research article reservoir characterization during underbalanced...
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Research ArticleReservoir Characterization during Underbalanced Drilling ofHorizontal Wells Based on Real-Time Data Monitoring
Gao Li1 Hongtao Li1 Yingfeng Meng1 Na Wei1 Chaoyang Xu1 Li Zhu1 and Haibo Tang2
1 State Key Laboratory of Oil and Gas Reservoir Geology and Exploration School of Petroleum EngineeringSouthwest Petroleum University Chengdu Sichuan 610500 China
2 Engineering Supervision Center SINOPEC Southwest Oil amp Gas Company Deyang Sichuan 618000 China
Correspondence should be addressed to Hongtao Li lihongtao053yahoocomcn and Yingfeng Meng cwctmyfvipsinacom
Received 4 April 2014 Accepted 15 July 2014 Published 17 August 2014
Academic Editor Vijay Gupta
Copyright copy 2014 Gao Li et al This is an open access article distributed under the Creative Commons Attribution License whichpermits unrestricted use distribution and reproduction in any medium provided the original work is properly cited
In thiswork amethodology for characterizing reservoir pore pressure and permeability during underbalanced drilling of horizontalwells was presented The methodology utilizes a transient multiphase wellbore flow model that is extended with a transient wellinflux analytical model during underbalanced drilling of horizontal wells The effects of the density behavior of drilling fluid andwellbore heat transfer are considered in our wellbore flow model Based on Kneisslrsquos methodology an improved method with adifferent testing procedure was used to estimate the reservoir pore pressure by introducing fluctuations in the bottom hole pressureTo acquire timely basic data for reservoir characterization a dedicated fully automated control real-time data monitoring systemwas established The methodology is applied to a realistic case and the results indicate that the estimated reservoir pore pressureand permeability fit well to the truth values from well test after drilling The results also show that the real-time data monitoringsystem is operational and can provide accurate and complete data set in real time for reservoir characterization The methodologycan handle reservoir characterization during underbalanced drilling of horizontal wells
1 Introduction
Underbalanced drilling has been used with increasing fre-quency in horizontal wells as it has conspicuous technicalsuperiorities compared to overbalanced drilling in decreas-ing drilling costs preventing invasive formation damageachieving higher rates of penetration and reducing drillingproblems such as pressure differential pipe sticking and lostcirculation [1 2] During underbalanced drilling the bottomhole pressure is kept below the reservoir pore pressureAs a result the reservoir will transport fluids towards thewellbore generating a transient well influx during drillingThe influx behavior of reservoir fluids depends on thepressure difference between the reservoir pore pressure andthe bottom hole pressure and reservoir permeability andporosity in addition to other reservoir parameters such as theviscosity and compressibility of reservoir fluidsThe transientwell influx causes flow behavior variations in the wellboreOwing to the changes in well fluid composition and well
fluid flow rates the transient influx of reservoir fluids cau-ses variations in the flow in the wellbore Analogous to welltesting and transient reservoir analysis the reservoir char-acteristics close to the well causing the influx might beidentified on site by monitoring some of the fluid flow dataof the well such as pressure changes and rate changes [3 4]This is the principal idea that also is the basis for reservoircharacterization during underbalanced drilling Estimationof the near wellbore characteristics of the formation givesimportant information for planning well completion designwell pressure control and optimizing drilling parameters onsite such as the wellrsquos horizontal length gas injection volumeand orientation
Reservoir characterization during underbalanced drillingstill needs strong theories to be formulatedwith reliable smartexperiments The complexity of this subject arises from thefact that the boundary conditions of transient well inflowchange with time during the test and that the rates of trans-ient well influx are influenced by variation in underbalance
Hindawi Publishing CorporationJournal of Applied MathematicsVolume 2014 Article ID 905079 19 pageshttpdxdoiorg1011552014905079
2 Journal of Applied Mathematics
Moreover the exhaustive and reliable monitoring data arenot easy to be acquired in real time To the best of theauthorsrsquo knowledge the idea that reservoir characterizationwhile underbalanced drilling was first presented by Kardolusand van Kruijsdijk [5] in 1997 In their paper a transientreservoir influx model of a vertical well under a constantunderbalance based on the boundary element method wasdeveloped They compared the model with a transient ana-lytical reservoir model and demonstrated that the transientanalytical reservoir model could be used for evaluatingcharacteristic parameters in the reservoir in particular thepermeability In a following study van Kruijsdijk and Cox [6]developed a method for identifying the permeability profilesalong the well trajectory of a horizontal well considering thevariable underbalance and themore complex outer boundaryconditions of a horizontal well
Reservoir characterization during underbalanced drillinghas been investigated by several other researchers in recentyears Larsen and Nilsen [7] proposed a simple quasi-stationary model for predicting the inflow at various levelsof complexity and accuracy for spreadsheet and calculatorapplications based on drilling speed and knowledge of theratio of vertical to horizontal permeability The influx pre-dictions calculated by their model and a numerical reservoirsimulator were compared giving a good agreement Azar-Nejad [8] presented a model for influx predictions using thediscrete flux element method In his study he mentionedfactors affecting influx rates and indicated that the solutionsof model are very sensitive to the reservoir thickness Huntand Rester [9 10] developed and solved new reservoirmodelsdescribing the underbalanced drilling problem and charac-terizing the dynamic changes in single layer andmultilayeredreservoirs They also presented a history matching methodfor predicting the reservoir permeability Biswas et al [11]proposed a genetic search algorithm for identifying thereservoir characterization accounting for storage effects inboth the wellbore and reservoir In a paper by Vefring et al[3] a transient reservoir model coupled to a transientwellbore flow model was used They estimated the reservoirproperties using novel Levenberg-Marquardt algorithm anonlinear least-squares optimization method In a follow-up research [4] the ensemble Kalman filter was also usedto predict reservoir pore pressure and reservoir permeabilitywhile applying active tests and comparedwith the Levenberg-Marquardt algorithm A paper by Kneissl [12] presented amethod of simultaneously deriving reservoir pore pressureand permeability profiles in real time during underbalanceddrilling by introducing fluctuations in the bottom holepressure during drilling However the variations of fluid flowbehavior in the wellbore might pose difficulties in estimatingthe influx rates which may lead to large uncertainties inthe estimate of reservoir pore pressure [13] Stewart et al[14] proposed an integrated transient model of the formationand the wellbore based on superposition The method ofmatching the cumulative production data for estimatingpermeability using iterative search was also developed intheir paper However an assumption that the pore pressureis known independently was made analogously like mostof above researchers The problem at hand is complex [11]
Although many models and methods for identifying reser-voir characterization while underbalanced drilling have beenproposed the interpretation of reservoir properties is difficultin real reservoirs particularly in real time except for thesimplest cases
This paper describes a new pursuit of the complexproblem of identifying the reservoir characterization duringunderbalanced drilling of horizontal wells A model oftransient well influx of horizontal wells is used together witha multiphase wellbore flow model The effects of the densitybehavior of drilling fluid and wellbore heat transfer duringunderbalanced drilling are considered in our wellbore flowmodel Based on the Kneisslrsquos methodology an improvedmethod of estimating reservoir pore pressure performedby introducing fluctuations in the bottom hole pressure bymanipulating the choke valve opening and changing fluidcomposition or pump rates is presented in this paper Aneffort is also made to monitor accurately and automaticallymeasurements required for reservoir characterization in realtime
The paper is organized by first presenting the real-timedata monitoring Then the transient wellbore flow modeland transient well influx model are presented respectivelyBased on the data monitoring and mathematical modelswe then propose the methodology for estimating reservoircharacterization In this paper the reservoir pore pressureand permeability profiles are the main reservoir propertiesneeded to be characterizedThemethodology is then appliedto a realistic case and results are discussed Thereafter aconclusion is made
2 Real-Time Data Monitoring
The accurate and automatic acquisition of basis data inreal time has been a challenge for reservoir characteriza-tion during drilling of horizontal wells which is crucialand is a prerequisite During a standard underbalanceddrilling operation lots of indispensable parameters can berecorded by the compound logging and other measuringequipment such as the density and rheology of the drillingfluid well depth penetration rate pump pressure outletrates trajectory of the well and wellbore diameter Howeverthese measurements are insufficient and not accurate enoughfor reservoir characterization Being more pivotal most ofthese measurements cannot be acquired in real time whichis indispensable to identifying reservoir characterizationduring drilling This paper has presented a dedicated fullyautomated control real-time data monitoring system basedon the integration and modification of existing devices orcomponents and the installation of some more indispensablesensitive and accurate measuring instruments In addition toinstalling somemeasuring equipment monitoring indispens-able parameters for reservoir characterization unrecordedgenerally in conventional drilling the data from com-pound logging and PMWDMWD are involved in our real-time monitoring system It is believed that the integrationis also beneficial for well control and drilling parameter
Journal of Applied Mathematics 3
optimization in underbalanced operations The measure-ments of interest here are as follows
(i) injection and outlet drilling fluid densities(ii) injection and outlet drilling fluid rates(iii) drilling fluid viscosity(iv) oil outlet rates and density(v) penetration rate in the formation(vi) injection and outlet gas rates pressure and tempera-
ture(vii) outlet gas component(viii) standpipe and surface casing pressure(ix) bottom hole pressure(x) measured depth and wellbore diameter(xi) BHA and hole trajectory(xii) formation porosity
Schematics of the location of the real-time data moni-toring system with respect to the well for aerated drillingand liquid-based underbalanced drilling are illustrated inFigures 1 and 2 respectively In order to explain the datamonitoring systems clearly it is necessary to first introducethe circulation process for underbalanced drilling Duringaerated drilling operations drilling fluid from mud pits andnitrogen from gas injection system consisting of compressornitrogen generator and booster are mixed and injected intothe drill strings under pressure via a fluid line as shown inFigure 1 The gasified drilling fluid is then circulated out withthe produced formation fluid through the annulus into theprimary flow line and enters the separator where gas and oilare separated The drilling fluid returns to the mud pits viaa return line after taking out the solids using shale shakersProduced oil is sent to an oil shimming tank Separated gasis sent to a combustion cell For liquid-based underbalanceddrilling the circulation process is somewhat different becauseonly drilling fluid is injected as shown in Figure 2 Thusthe measurements of the gas injection rates pressure andtemperature were not involved in the data monitoring systemfor liquid-based unbalanced drilling For the reason that theattenuation of drilling fluid pulse in multiphase flow restrictsthe use of down hole measuring devices with transmissionmedium of drilling fluid pulse in aerated drilling [16 17]PMWDMWDdatawere not included in the datamonitoringsystem for aerated drilling
As shown in Figures 1 and 2 the real-time data monitor-ing systems consist of various kinds measuring instrumentsan incoherent receptor a signal converser and a PC Toacquire various parameters in different types in real time themeasuring facilities used here include pressure transducerstemperature transducer gas and liquid flowmeters densitymeasuring unit and portable gas analyzer The strong tech-nology and sophisticated equipment were applied in dataacquisitions in this paperThe pressure transducers used herehave a frequency response of 01sim1000Hz and a maximumfull scale output error of 075 FSO over the 0 to 70∘Ccompensated rangeThe injection and outlet gas temperature
was measured by the temperature transducers with widetemperature range from minus55∘C to +150∘C and excellentlinearity of plusmn03∘C In order to assure measurement accuracydifferent types of portable type clip ultrasonic flowmeter wereclamped on to the existing pipeline to acquire respectivelythe drilling fluid oil and gas rates The density measuringunit proposed by Carlsen et al [18] consisting of threepressure transducers placed along the circulating path fromthe pump to the connection to the drill string was usedto identify automatically the injection drilling fluid densityAn advantage of this method is that it enables automaticupdates of the density Likewise the outlet drilling fluiddensity can readily be determined The density of outlet oilwas measured using a common method for the reason that itis relatively fixed for a particular reservoir The acquisition ofoutlet gas component can be completed using a portable gasanalyzer One of the technical superiorities of this system isthat a digital microwave transmission technique was used totransmit the data recorded by various measuring equipmentinstead of the use of the cable All the measuring instrumentsshown in Figures 1 and 2 were attached to a wireless radiatedelement respectively Measurement signals from pressuretransducers flowmeters and other instrumentswere receivedwirelessly by an incoherent receptor and then analyzed andrecorded using a signal analyzer after being converted intodigital signals It is noted that the incoherent receptiontechnique indicated in Spalding and Middleton [19] wasapplied here to tackle the reception of signals in the impulsiveinterference environment Data acquisition software calledLabVIEW was used to capture the measurement signalsThese measurements together with compound logging dataand PMWDMWD data were preprocessed to detect neces-sary information for reservoir characterization in standarddata formats usingMATLAB on a personal computer Owingto the use of wireless transmission technique the signalreceptor and data processing system no longer have to belocated near the well site which makes remote supervisoryand technical service possible The work above in this paperensures that the data are accurate real time and easilyavailable which is critical and considerable for reservoircharacterization during drilling
3 Transient Wellbore Flow Model
The wellbore transients have significant effect on actualwell inflow and therefore should be considered in reservoircharacterization The real-time data monitoring system canprovide bottom hole pressure in liquid-based underbalanceddrilling During aerated drilling the wellbore transientsmust be calculated by mathematical means owing to theserious attenuation of PMWD signals In this section a one-dimensional liquid-gas two-phase transient model governingwellbore flow with thermal effects in aerated drilling isdeveloped with variables resolved in the axial direction onlyBesides the effect of the cutting bed in horizontal sections isconsidered Owing to complexity of the liquid-gas two-phaseflow transient in wellbore the following assumptions madefor the model development are primarily given
4 Journal of Applied Mathematics
Choke manifold Combustion cell
Three-wayvalve
ThrottleMud pumps
BlenderThrottle
Portable gasanalyzer
Liquidflowmeter
Liquid flowmeterShale
shakers
Pressure transducer
Reserve pit
Mud pits
Pressuretransducer
Sampling
Booster
PC Reservoir characterization Compound logging data
Oil skimming tank
11
Sampling
Signal converser Incoherent receptor
Density measuring unit
Temperature transducer
Pressure transducer
Signal analyzer
Outlet (oil)
Pressure transducer
Gas flowmeter
Density measuring
unit
Throttle
Separator
Liquid flowmeter
Gas flowmeter
Injection (mud)
Drillstrings
Annulus
Injection(gas)
Injection(mixture)
Outlet
Outlet (mud)
Outlet (gas)
Outlet (mud)
Primary flow line
RBOP
Secondaryflow line
Nitrogengenerator
Compressor
Atmosphere
Solids disposal
Mud return line
Temperature transducer
deg100
50
minus0
minus10mV
Figure 1 A schematic of the placement of the real-time data monitoring system for aerated drilling
deg
Choke manifold Combustion cell
Three-wayvalve
ThrottleMud pumps Portable gas
analyzer
Liquidflowmeter
Liquid flowmeterShale
shakers
Pressure transducer
Reserve pit
Mud pits
Pressuretransducer
Sampling
100
50
PC Reservoir characterization Compound logging data
Oil skimming tank
11
Sampling
Signal converser Incoherent receptor
Density measuring unit
Pressure transducer
Signal analyzer
Outlet (oil)
Density measuring
unit
Throttle
Separator
Liquid flowmeter
Gas flowmeter
Injection (mud)
Injection (mud)
Mud return line Drillstrings
Annulus
Outlet
Outlet (mud)
Outlet (gas)
Outlet (mud)
Temperature transducer Primary flow line
RBOP
Secondaryflow line
Solids disposal
minus0
minus10mV
Figure 2 A schematic of the placement of the real-time data monitoring system for liquid-based underbalanced drilling
(i) The liquid phase fluids are incompressible and New-tonian
(ii) Properties of fluids are uniform and constant
(iii) The bubbles are spherical in shape having diameter asthe characteristic
(iv) The transverse lift force is neglected
(v) The turbulent dispersion force of gas phase is neglec-ted
(vi) The effects of breakup and coalescence of droplets andbubbles are neglected
(vii) Mass transfer effects are neglected
31 Model Development In this paper a transient model ofliquid-gas two-phase flow in wellbore is proposed on thebasis of the three-dimensional model averaged in time andspace given by Lahey andDrew [20]The governing equationsconsist of continuity equations for each component and a
Journal of Applied Mathematics 5
momentum conservation equation Such equations can bewritten as follows
gas continuity equation
120597 (120588
119892120572
119892)
120597119905
+
120597 (120588
119892120572
119892119906
119892)
120597119911
= 0
(1)
liquid continuity equation
120597 (120588
119897120572
119897)
120597119905
+
120597 (120588
119897120572
119897119906
119897)
120597119911
= 0(2)
gas momentum conservation equation
120597 (120588
119892120572
119892119906
119892)
120597119905
+
120597 (120588
119892120572
119892119906
2
119892
)
120597119911
+ 120572
119892
120597119901
120597119911
= minus120572
119892120588
119892119892 sin 120579 minus 119865
119889119892minus 119865V119898 minus 119865
119908119892
(3)
liquid momentum conservation equation
120597 (120588
119897120572
119897119906
119897)
120597119905
+
120597 (120588
119897120572
119897119906
2
119897
)
120597119911
+ 120572
119897
120597119901
120597119911
= minus120572
119897120588
119897119892 sin 120579 minus 119865
119889119892minus 119865V119898 minus 119865
119908119897
(4)
where 119901 is pressure 119892 is the acceleration due to gravity 120588is density 119906 is velocity 120572 is the volumetric fraction 120579 is thedeviation angle 119905 and 119911 are temporal and spatial coordi-nates 119865
119889is drag force 119865V119898 is virtual mass force 119865
119908is
wall shear force and the subscripts 119892 119897 represent gas andliquid respectively The indispensable closure relationshipsappearing in equations above are formulated and describedin Appendix A
Due to the mixture of gas-liquid two phases the dis-tribution relation of two-phase homogeneous fluid can benormalized as
120572
119892+ 120572
119897= 1 (5)
In this paper gas phase can be deemed as the ideal gas andcan be evaluated using the equation of state in the followingmanner
119901 = 119885120588
119892119877119879 (6)
where 119879 is temperature 119877 denotes the gas constant and 119885 isthe real gas deviation factor which is the function of pressuretemperature and the nature of the gas
In the transient liquid-gas two-phase flow model theheat transfer between wellbore and formation is consideredby introducing a wellbore heat transfer model during two-phase flow presented by Hasan and Kabir [21] based on arigorous energy balance equation for two-phase flow [22] Anexpression for fluid temperature in wellbore as a function ofwell depth and producing time is primarily given by
119879 = 119879
119890119894+ 120585 [1 minus 119890
119867120585
] (
119892
119892
119888
sin 120579
119869119862
119901
+ 120593 + 119892
119879sin 120579)
+ 119890
(119867minus119911)120585
(119879
119891119887ℎminus 119879
119890119887ℎ)
(7)
where 119879
119890119894is undisturbed formation temperature at given
depth 120585 is inverse relaxation distance 119867 is total welldepth from surface 119892
119888and 119869 represent conversion factors
119862
119901is the mean heat capacity of the multiphase fluid at
constant pressure 119892119879is geothermal temperature gradient
120593 is parameter combining the Joule-Thompson and kineticenergy effects 119879
119891119887ℎis fluid temperature at the bottom hole
and 119879
119890119887ℎis formation temperature at bottom hole Some
important parameters are discussed in detail in Appendix BIn the transient wellbore flow model we consider the
density behavior of drilling fluid under high pressure andhigh temperature conditions during underbalanced drillingoperation A more accurate analytical model for density-pressure-temperature dependence for drilling fluid in drillingproposed by Karstad and Aadnoy [23] was presented in thefollowing manner
120588
119897= 120588
119897119904119891119890
120574119901(119901minus119901119904119891)+120574119901119901(119901minus119901119904119891)2+120574119879(119879minus119879119904119891)+120574119879119879(119879minus119879119904119891)
2+120574119901119879(119901minus119901119904119891)(119879minus119879119904119891)
(8)
where 120588
119897119904119891is the drilling fluid density under standard con-
ditions 119879119904119891
is the standard temperature 120588119904119891
is the standardpressure and the values of 120574
119901 120574
119901119901 120574
119879 120574
119879119879 and 120574
119901119879are
essentially unknown and must be determined for differentmuds from density measurements at elevated pressures andtemperatures
Though we have made an assumption of gas liquid two-phase flow in wellbore the effect of cutting bed in horizontalwell on wellbore flow simulation has to be considered Thecutting bed existing in the horizontal annulus reduces theopen flow area of gas liquid two-phase fluid which is acritical factor in wellbore flow simulation In this paper weconsider the effect of cutting bed by evaluating the open flow
area of gas liquid two-phase fluid in horizontal annuluscausing the movement of cutting bed The cuttings trans-port in horizontal wellbore has been investigated by manyresearchers [24ndash30] In this paper we use a mechanics modelwith aerated drilling fluid proposed by Zhou [30] to predictthe movement of cutting bed and the cutting bed height
32 Numerical Solution In order to solve the model thefinite difference technique which is one of the most widelyused numerical methods is applied in this paper Thetechnique is implemented by replacing all derivatives bydifference quotients Owing to the introduction of analyticalexpression of temperature the model is easier to solve using
6 Journal of Applied Mathematics
the technique Discretization of governing equations can beobtained applying a first order downstream implicit schemefor time derivations For the stability of numerical solutionsthe donor cell concept is used The fluid exit conditions areassumed to be the same as the fluid conditions in the nodeitself The discretized form of governing equations can bewritten in the following matrix form
D119895(k0119895
) k119905+Δ119905119895
= E119895(k0119895
k119905119895
k119905+Δ119905119895minus1
) (9)
whereD is the coefficient matrix E is the independent vector119895 is cell number the superscripts 119905 and 119905+Δ119905 are the dependentvariables calculated at the old and new times respectively thesuperscript 0 represents the dummy variables for the iterativemethod and v is a column vector of dependent variablesgiven as follows
v = (119901 120572
119892 119906
119892 119906
119897)
119879
(10)
where the superscript 119879 indicates the transposeMechanistic models for two-phase flow in drill string and
annuli [31ndash33] are used to provide the necessary informationfor numerical calculation about flow patterns pressure dropsphase volumetric fractions and phase velocities in each oldtime node The wellbore fluid temperature at each grid pointcan be estimated using (7) In this paper we use the algorithmbased on the factorization of a matrix using a version of theGaussian elimination with partial pivoting
It is important to note that the numerical solution istransient due to the fact that almost all the transient termsare considered in our model In addition the numericalsolution of two-phase wellbore flow under constantly chang-ing flowing environmental can be given easily owing to theestablishment of real-time data monitoring system
4 Transient Well Influx Model
In underbalanced drilling the transient well influx can bedeemed as a complex well test The complexity arises fromthe fact that the boundary conditions vary with times invalue and type during the test because the well is con-tinuously increasing in length In the drilled part of thereservoir we have a Dirichlet boundary condition Insteadthe Neumann boundary condition is dealt with along thefuture well trajectory in the reservoir Also keep in mindthat the transient influx rates are influenced by variation inunderbalance and penetration rateTherefore the traditionalwell test techniques are not fit for the purpose of modelingtransient well influx during underbalanced drilling Becauseof the complexity of the problems a realistic model is neededto predict the transient well inflow while drilling
41 Mathematical Model Themodel in this paper representsa simplification of the actual reservoir It is assumed thatthe reservoir is symmetric around the well and possessesconstant reservoir and parameters During the transientperiod we assume that there is no pressure response from theborder of the reservoir For transient flow of a single phase
the governing differential equation can be given in the formof diffusivity equation
nabla
2
119901 =
120601120583119888
119896
120597119901
120597119905
(11)
where 120601 is porosity 119888 is reservoir compressibility 120583 is theviscosity of reservoir fluid and 119896 is the reservoir permeability
With the above assumption that there is no pressureresponse from the border of the reservoir the outer boundaryis given in the following Neumann manner
120597119901
120597119899
= 0(12)
where 119899 is the normal of the boundary surfacesEssentially the main difference of transient influx during
drilling with convention well test operations lies in the innerboundary which changes with time For the part of thereservoir penetrated by a horizontal well we have a Dirichletboundary condition
119901 = 119901
119908ℎ (13)
where 119901119908ℎ
is the pressure at bottom holeFor the undisturbed part of the reservoir the influx rates
are zero in other words the inner boundary conditionslikewise can be captured by the above Neumannmanner It isimportant to note that as a result of the continuous increasein well length the inner boundary conditions do not onlychange in value but in types as well Every drill step the partof the reservoir that is dominated by the Neumann conditiondecreases while the zone governed by theDirichlet conditionincreases This means that we have to deal with a new set ofequations with different boundary conditions for every stepdrill stepThus we are in dire need of new realistic expressionto describe the transient well influx during underbalanceddrilling
42 Approximate Analytical Solution To allow analyticalsolutions of the transient influx problem some essentialhypotheses are made in this paper We assume that thereservoir consists of a number of independent elements orzones as shown in Figure 3 It is assumed that the fluidflows along planes perpendicular to the well During under-balanced drilling a new zone is added to the well everystep in time The size of the time step and the thickness ofdrilled zones must conform to the penetration rate which isconsidered to be constant here It is assumed that productionfrom new added zone starts at the moment when it is beingpenetrated by drilling The total production rate at a giventime can be obtained by adding the production response ofindividual zones that time Thus the total production rate asa function of time can be given by
119902
119905119900119905(119905) = int
119911(119905)
0
119902
119908(119911 119905) 119889119911
(14)
Journal of Applied Mathematics 7
InjectionOutlet
Undisturbedreservoir
Opened reservoir elements
Permeability k1 k2 k3 k4
k1 k2 k3 k4
Figure 3 A schematic of a horizontal well drill into the reservoirconsists of a number of independent elements
where depth 119911 is a function of time 119905 and the penetrationrate 119906
119901 and 119902
119908(119909 119905) is the well influx from a unit thickness
Substitution of 119889119911 = 119906
119901119889119905 yields
119902
119905119900119905(119905) = int
119905
0
119902
119908(119911 120591) 119906
119901119889120591 (15)
Using Duhamelrsquos theorem van Kruijisdijk and Cox [6]proposed that the transient well influx for a given elementcan be rendered to a convolution of the underbalance andthe time derivative of the well influx for a constant andunit underbalance and rewrote the above equation in thefollowing manners
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (119901
119903119890119904minus 119901
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(16)
where 119902
119908119906(119905) denotes the unit-underbalanced inflow of unit
reservoir segment at the given time Θ represents the setof reservoir parameters that define the flow geometry andproperties 119901
119903119890119904is the reservoir pore pressure and 119901
119908is a
function of time and is defined as
119901
119908(119905) =
119901
119903119890119904for 119905 le 119905open (119911)
119901
119908ℎ(119905) for 119905 gt 119905open (119911)
(17)
The function 119905open(119911) represents the time atwhich the drillbit penetrates point 119911 thereby opening that point along thewell trajectory up to flow
To obtain an analytical solution of transient well inflowat any given time we need a realistic expression of the unit-underbalance transient inflow of each unit thickness segment119902
119908119906(119905) Based on the appropriate source functions in Laplace
space van Kruijisdijik [34] proposed the following analyticalsolution
119902
119908119906(119905) =
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(18)
where ℎ is the reservoir thickness 119903119908is the radius of the
wellbore119861119900is the volume factor of the reservoir fluid 119878
119911is the
effective skin due to vertical flow 1198861and 119886
2are the coefficient
and have respectively the values of 0611 and 1083 in the earlytime of transient influx
For gas reservoir the expression of the transient inflowis a bit different from (16) the analytical solution for oilreservoir proposed by van Kruijisdijk and Cox [6] Thecompressibility of gas decides the influx difference betweenoil and gas reservoirWe define the pseudopressure as follows
= 2int
119901
1199010
119901
120583
119892(119901)119885 (119901)
119889119901 (19)
where 119901
0is the known pressure for reference 120583
119892is the gas
viscosity and 119885 is the compressibility factor of the gas Thenthe total influx rates of gas reservoir during underbalanceddrilling can be given
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (
119903119890119904minus
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(20)
Analogously we rewrite the analytical expression of 119902119908119906
forgas reservoir in the following manner
119902
119908119906(119905) =
120587119896ℎ
119861
119892
119885
119904119888119879
119904119888120588
119892119904119888
119901
119904119888119879
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(21)
where the subscript denotes the standard state
5 Methodology of EstimatingReservoir Characterization
After establishing datamonitoring system in real time a tran-sient liquid-gas two-phase flow model in wellbore and wellinflux model during drilling have been derived Hereuntowe have reliable data acquisition approach and theoreticalmodel for reservoir characterization In this section let usfocus on specific approach to estimate reservoir properties Atfirst we will propose a new methodology to acquire reservoirpore pressure and then discuss how to extract the reservoirpermeability profiles during drilling
51 Reservoir Pore Pressure Inspired by the interestingmethodology of identifying reservoir pore pressure proposedby Kneissl [12] a new improved method of testing reservoirpore pressure is developed using different testing procedureavoiding the uncertainties affected by variations of fluid flowbehavior in the annulus sections and unpredictable inflowof new added zones It is noted that the idea of identifyingreservoir pore pressure by actively fluctuating the bottomhole pressure is still the key kernel thought of our methodFocusing on the new methodology a principal assumptionhas to be made that the reservoir drilled consists of differentzones with constant formation pressure coefficient whichcorresponds with the most common circumstances Withthe continuous pressure system assumption it is easy to
8 Journal of Applied Mathematics
obtain reservoir pore pressure of each zone by extracting thereservoir pressure coefficient when the reservoir is openedThis greatly simplifies the procedure of pore pressure testand avoids complex mathematical computation usually usedin other methods To eliminate the uncertainties of estimateresults introduced by continuous inflow of new zones it isneeded to stop drilling but keep circulation to begin thetesting operation when the first reservoir zone was openedwhich is the difference from Kneisslrsquos method in testingprocedure Taking into account the fact that only the first zonewas opened in the testing operation the transient inflow ofwell can be given by
119902
119908(119905) =
2120587119896ℎ (119901
119903119890119904minus 119901
119908(119905))
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(22)
It can be rewritten as
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(23)
At very short time the expression reduces to the followingmanner
lim119905rarr0
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
= lim119905rarr0
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911
(24)
which is entirely independent of the time and the downside of the equation can be considered constant for a givenreservoir It also can be interpreted that the transient inflowof well has a significant negative linear correlation with thepressure at bottom hole in the earliest hours of inflow Forthe inflow of well to become zero the reservoir pore pressureis approached by the pressure at bottom hole Thence wecan identify the reservoir pore pressure by searching forthe linear correlation between the inflow and pressure atbottom at the early stage of transient inflow This processis performed by introducing artificially fluctuations in thebottom hole pressure and by measuring the inflow rates andbottom hole pressure based on the real-time data monitoringsystem For aerated drilling the bottom hole pressure can beestimated using the transient wellbore flowmodel mentionedin this paper Figure 4 illustrates some details concerninghow to extract the reservoir pore pressure Here linear fittingof some measurement points is used to identify the linearcorrelation between thewell inflow and bottomhole pressureand the reservoir pore pressure can be read at the crossingof the best-fit regression line and the horizontal axis Forthe reliability of test results the number of testing pointsshould not be less than three Fluctuations of the bottom holepressure can be introduced by managing the choke valvechanging gas injection rates or pump rates To eliminatethe effects of variations of fluid flow in the wellbore onthe estimated results it is necessary to leave enough timeto capture relative steady inflow rates for each fluctuating
High
High
Low
0
qw
pw
Testing dataBest-fit regression line
Reservoir pressure
Figure 4 Reservoir pore pressure test by introducing fluctuation atthe bottom hole pressure
operation and the time needed lasts for a few minutes ormore than one hour which depends on well depth the typeof operations introducing the fluctuation in the bottom holepressure reservoir characteristics such as permeability andformation fluid properties and so on
Having acquired the reservoir pore pressure of the firstzone when the reservoir is opened the reservoir pressurecoefficient and pressure of subsequent zones can be obtainedduring drilling using a simple formula For the case wheremore than one reservoir with different pressure system wasdrilled new testing procedure should be repeated when newreservoir was opened The only difference is that the inflowmeasurements consist of the transient inflow response ofthe former reservoir and the transient well inflow of newreservoirrsquos first zone Here necessarymathematical treatmentof the inflow measurements is needed
52 Permeability Profiles To determine the reservoir perme-ability we make the simplifying assumption that the perme-ability is constant in specified zones of the well Transientinflux from each reservoir zone with different permeabilityat the time of interest constitutes the total production rates ofthewell which can be got from the real-time data acquisitionssystem The analytical expressions of total production ratesand unit-underbalance response of each zone which arerelated to the permeability have been established in the lastsection of this paper The reservoir pore pressure of eachreservoir zone can be calculated after testing the reservoirpressure coefficient just when the reservoir was opened Itis assumed that the porosity reservoir height and otherreservoir parameters apart from permeability are constantand known Theoretically the permeability of each reservoirzone can be easily determined using (18) and (21) Unfor-tunately the analytical expressions of the total productionrates are given in integral form which results in that theycannot readily be implemented in spreadsheet and calculator
Journal of Applied Mathematics 9
applications To facilitate the calculation a full discretizationof the total production rates formula is given instead of theintegral form in the following manner
119902
119905119900119905(119905) = 119906
119901(119901
119903119890119904minus 119901
119908)
119899=119905Δ119905
sum
119894=1
119902
119908119906119894(Θ
119894 119905 minus 119905
119894) Δ119905 (25)
where Δ119905 represents the time needed to penetrate througha reservoir element which is constant with the assumptionof the fixed penetration rate 119902
119908119906119894(Θ
119894 119905 minus 119905
119894) denotes unit-
underbalanced inflow of unit reservoir segment from zone 119894and 119905
119894denotes the time the wellbore reaches zone 119894 The value
of 119902119908119906119894
(Θ
119894 119905 minus 119905
119894) for nonpositive arguments is set equal to 0
The above discretization equation was given on the basisof a reasonable assumption that we have a constant underbal-ance which is realistic and is of engineering significance forunderbalanced drilling of a horizontal well
First we discuss how to extract the permeability of the1st reservoir zone The total production rates from the real-time monitoring system at the first time step when reservoiris opened can be simply considered to be the influx from thefirst zone Then we have the following formula
119902
119905119900119905(119905
1) = 119902
1199081(119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) 119902
1199081199061(Θ
1 119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
1ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896Δ119905120601120583119888119903
2
119908
(26)
Solving the equation above 1198961 the permeability of the 1st
reservoir zone can be given as follows
119896
1= (119898
2119902
1199081(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
1199081
(119905
1) Δ119905 +
119902
1199081(119905
1) 119878
119911
119898
1
)
2
(27)
where
119898
1=
2119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) ℎ119886
1
120583119861
119900119903
119908
119898
2=
119886
2
2119898
1119903
119908
radic120601120583119888
(28)
Analogously well influx from the reservoir element 119894 canbe given
119902
119908119894(119905
1)
= 119902
119905119900119905(119905
119894) minus
119894minus1
sum
119899=1
119902
119908119899(119905
119894minus119899)
= 119902
119905119900119905(119905
119894) minus 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
119894minus1
sum
119899=1
119902
119908119906119899(119905
119894minus 119905
119899)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
119894ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896
119894Δ119905120601120583119888119903
2
119908
(29)
where 119902tot(119905119894) represents the total production rates of the wellat time 119905
119894when the reservoir element is opened 119902
119908119906119899(119905
119894minus 119905
119899)
denotes the unit-underbalance transient influx response ofunit thickness reservoir from reservoir zone 119899 at time 119905
119894and
can be given using (21)Then we can extract the permeability of the reservoir
zone 119894 by
119896
119894= (119898
2119902
119908119894(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
119908119894
(119905
1) Δ119905 +
119902
119908119894(119905
1) 119878
119911
119898
1
)
2
(30)
Using the methodology the permeability of a set ofreservoir zones can be successively extracted as the reservoiris being penetrated by a horizontal well To facilitate theprecise calculation and estimate permeability profiles in timea computer procedure was used in this paper The success ofreservoir permeability estimation profits from reliable real-time data monitoring system advanced wellbore flow andreservoir model and an innovative reservoir pore pressuretest approach
6 Results and Discussion
The methodology presented in this paper has been used toidentify the reservoir pore pressure and permeability profilesof approximately 10 wells during underbalanced drilling inChina In order to illustrate the above approach in detail anactual horizontal well and gas reservoir are considered in thissection It is appropriate to emphasize that the well picked ascase study is the first successful application of this method-ology More exhaustive data and offset information from thiswell facilitate the effectiveness evaluation of this methodThereservoir dealt with here is the Ordovician carbonate gasreservoir with natural fractures as the dominant gas storagespaces and flowing channels To avoid lost circulation andformation damage the well is drilled underbalanced usingthe aerated clay-free drilling fluid while this is also beneficialfor well control Here nitrogen is used as the injection gasThe hole geometry and drilling assembly of this well wereillustrated in Figure 5 Some basic parameters for reservoirand drilling fluid used in reservoir characterization wereshown in Table 1
61 Data Acquisition in Real Time The real-time data mon-itoring system for aerated drilling presented in this paperwas used to acquire basic data for reservoir characterizationin real time The application of this system guaranteesthat the indispensable parameters are accurate and timelywhichmakes it possible to identify reservoir characterizationDuring drilling this system succeed in the integration of thedata from compound logging and our sensitive measuringinstruments and the digital microwave transmission wasproved to be realizable and reliable to deliver wirelesslydata Some typical acquired measurements plotted againsttime are shown in Figures 6ndash10 In order to illustrate thetransient behavior for different parameters the measuringtime for different parameters in figures differs The standpipe
10 Journal of Applied Mathematics
Drill bit
Cement
Casing
Drill strings
Wellhead
Bottom holeBarefoot interval
Annulus
Protective casing interval
Drill strings size
Diameter 01524m
Diameter 01524mDepth 4000ndash4960m
Inner diameter 022m
Outside diameter 01397mInner diameter 01214m
Outside diameter 00889mInner diameter 00702m
Outside diameter 00889mInner diameter 00381m
Depth 0ndash
Depth 0ndash1800m
Depth 1800ndash4930m
Depth 4930ndash4960m
4000m
Figure 5 The hole geometry and drilling assembly of the well
Table 1 Basic parameters for reservoir and drilling fluid used inreservoir characterization
Depth evaluation of the reservoir m 4156Reservoir thickness m 15Porosity 12Reservoir fluid volume factor m3stdm3 0008Reservoir fluid viscosity mPasdots 0035Reservoir compressibility Paminus1 116 times 10minus9
Reservoir fluid compressibility Paminus1 1177 times 10minus9
Geothermal temperature Ksdotmminus1 003Drilling fluid density at standard conditions gsdotcmminus3 104Drilling fluid viscosity at standard conditions mPasdots 20Injection gas specific gravity 1 097Injection gas viscosity at standard conditions mPasdots 0019
pressure and casing pressure for different time are plottedrespectively in Figures 6 and 7 It can be seen that thetransient fluctuations of standpipe pressure are more acutethan that of casing pressure In general this difference canbe aroused by unsteady drilling fluid and gas injection checkcalve measuring apparatus installed along drill string anddrill string vibrationThe casing pressure changing with timein Figure 7 indicates the different outlet gas rates or variedchoke opening Figure 8 shows the drilling fluid density asa function of time for outlet and injection respectivelyContrary to the standard drilling operations more accurateand automatic measurements of drilling fluid density can beobtained in real time utilizing instrumented standpipe andseparator drilling fluid outlet pipe using different pressure
2030 2118 2207 2254 234110
11
12
13
14
15
16
17
18
Stan
dpip
e pre
ssur
e (M
Pa)
Time1930
Figure 6 Data acquisitionmdashstandpipe pressure data versus time(2010-9-27)
1151 1342 1527 1715 1901 2052 2230250
275
300
325
350
375
400Ca
sing
pres
sure
(MPa
)
Time1000
Figure 7 Data acquisitionmdashcasing pressure data versus time (2010-9-27)
transducers not measured manually in intervals of 15 min-utes It is noted that the outlet drilling fluid density is slightlylower than that of injection fluid and fluctuates wildly Thistransient behavior of outlet drilling fluid density occurs as aresult of varied outlet gas rates and nonthorough degassing ofdrilling fluid In this study we monitor the total hydrocarboncontent of outlet gas and outlet gas rates to acquire thereservoir gas inflow rates in real timeThemeasured outlet gasrates and reservoir gas inflow rates are presented in Figure 9The real-time reservoir gas inflow rates absolutely criticalfor reservoir characterization are calculated using the outletgas rates and total hydrocarbon content in time of interestas shown in Figure 10 In sum the application of the newreal-time data monitoring system in this well helps drillingcontractor with good underbalanced drilling operations and
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
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Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
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Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
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International Journal of
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Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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Stochastic AnalysisInternational Journal of
2 Journal of Applied Mathematics
Moreover the exhaustive and reliable monitoring data arenot easy to be acquired in real time To the best of theauthorsrsquo knowledge the idea that reservoir characterizationwhile underbalanced drilling was first presented by Kardolusand van Kruijsdijk [5] in 1997 In their paper a transientreservoir influx model of a vertical well under a constantunderbalance based on the boundary element method wasdeveloped They compared the model with a transient ana-lytical reservoir model and demonstrated that the transientanalytical reservoir model could be used for evaluatingcharacteristic parameters in the reservoir in particular thepermeability In a following study van Kruijsdijk and Cox [6]developed a method for identifying the permeability profilesalong the well trajectory of a horizontal well considering thevariable underbalance and themore complex outer boundaryconditions of a horizontal well
Reservoir characterization during underbalanced drillinghas been investigated by several other researchers in recentyears Larsen and Nilsen [7] proposed a simple quasi-stationary model for predicting the inflow at various levelsof complexity and accuracy for spreadsheet and calculatorapplications based on drilling speed and knowledge of theratio of vertical to horizontal permeability The influx pre-dictions calculated by their model and a numerical reservoirsimulator were compared giving a good agreement Azar-Nejad [8] presented a model for influx predictions using thediscrete flux element method In his study he mentionedfactors affecting influx rates and indicated that the solutionsof model are very sensitive to the reservoir thickness Huntand Rester [9 10] developed and solved new reservoirmodelsdescribing the underbalanced drilling problem and charac-terizing the dynamic changes in single layer andmultilayeredreservoirs They also presented a history matching methodfor predicting the reservoir permeability Biswas et al [11]proposed a genetic search algorithm for identifying thereservoir characterization accounting for storage effects inboth the wellbore and reservoir In a paper by Vefring et al[3] a transient reservoir model coupled to a transientwellbore flow model was used They estimated the reservoirproperties using novel Levenberg-Marquardt algorithm anonlinear least-squares optimization method In a follow-up research [4] the ensemble Kalman filter was also usedto predict reservoir pore pressure and reservoir permeabilitywhile applying active tests and comparedwith the Levenberg-Marquardt algorithm A paper by Kneissl [12] presented amethod of simultaneously deriving reservoir pore pressureand permeability profiles in real time during underbalanceddrilling by introducing fluctuations in the bottom holepressure during drilling However the variations of fluid flowbehavior in the wellbore might pose difficulties in estimatingthe influx rates which may lead to large uncertainties inthe estimate of reservoir pore pressure [13] Stewart et al[14] proposed an integrated transient model of the formationand the wellbore based on superposition The method ofmatching the cumulative production data for estimatingpermeability using iterative search was also developed intheir paper However an assumption that the pore pressureis known independently was made analogously like mostof above researchers The problem at hand is complex [11]
Although many models and methods for identifying reser-voir characterization while underbalanced drilling have beenproposed the interpretation of reservoir properties is difficultin real reservoirs particularly in real time except for thesimplest cases
This paper describes a new pursuit of the complexproblem of identifying the reservoir characterization duringunderbalanced drilling of horizontal wells A model oftransient well influx of horizontal wells is used together witha multiphase wellbore flow model The effects of the densitybehavior of drilling fluid and wellbore heat transfer duringunderbalanced drilling are considered in our wellbore flowmodel Based on the Kneisslrsquos methodology an improvedmethod of estimating reservoir pore pressure performedby introducing fluctuations in the bottom hole pressure bymanipulating the choke valve opening and changing fluidcomposition or pump rates is presented in this paper Aneffort is also made to monitor accurately and automaticallymeasurements required for reservoir characterization in realtime
The paper is organized by first presenting the real-timedata monitoring Then the transient wellbore flow modeland transient well influx model are presented respectivelyBased on the data monitoring and mathematical modelswe then propose the methodology for estimating reservoircharacterization In this paper the reservoir pore pressureand permeability profiles are the main reservoir propertiesneeded to be characterizedThemethodology is then appliedto a realistic case and results are discussed Thereafter aconclusion is made
2 Real-Time Data Monitoring
The accurate and automatic acquisition of basis data inreal time has been a challenge for reservoir characteriza-tion during drilling of horizontal wells which is crucialand is a prerequisite During a standard underbalanceddrilling operation lots of indispensable parameters can berecorded by the compound logging and other measuringequipment such as the density and rheology of the drillingfluid well depth penetration rate pump pressure outletrates trajectory of the well and wellbore diameter Howeverthese measurements are insufficient and not accurate enoughfor reservoir characterization Being more pivotal most ofthese measurements cannot be acquired in real time whichis indispensable to identifying reservoir characterizationduring drilling This paper has presented a dedicated fullyautomated control real-time data monitoring system basedon the integration and modification of existing devices orcomponents and the installation of some more indispensablesensitive and accurate measuring instruments In addition toinstalling somemeasuring equipment monitoring indispens-able parameters for reservoir characterization unrecordedgenerally in conventional drilling the data from com-pound logging and PMWDMWD are involved in our real-time monitoring system It is believed that the integrationis also beneficial for well control and drilling parameter
Journal of Applied Mathematics 3
optimization in underbalanced operations The measure-ments of interest here are as follows
(i) injection and outlet drilling fluid densities(ii) injection and outlet drilling fluid rates(iii) drilling fluid viscosity(iv) oil outlet rates and density(v) penetration rate in the formation(vi) injection and outlet gas rates pressure and tempera-
ture(vii) outlet gas component(viii) standpipe and surface casing pressure(ix) bottom hole pressure(x) measured depth and wellbore diameter(xi) BHA and hole trajectory(xii) formation porosity
Schematics of the location of the real-time data moni-toring system with respect to the well for aerated drillingand liquid-based underbalanced drilling are illustrated inFigures 1 and 2 respectively In order to explain the datamonitoring systems clearly it is necessary to first introducethe circulation process for underbalanced drilling Duringaerated drilling operations drilling fluid from mud pits andnitrogen from gas injection system consisting of compressornitrogen generator and booster are mixed and injected intothe drill strings under pressure via a fluid line as shown inFigure 1 The gasified drilling fluid is then circulated out withthe produced formation fluid through the annulus into theprimary flow line and enters the separator where gas and oilare separated The drilling fluid returns to the mud pits viaa return line after taking out the solids using shale shakersProduced oil is sent to an oil shimming tank Separated gasis sent to a combustion cell For liquid-based underbalanceddrilling the circulation process is somewhat different becauseonly drilling fluid is injected as shown in Figure 2 Thusthe measurements of the gas injection rates pressure andtemperature were not involved in the data monitoring systemfor liquid-based unbalanced drilling For the reason that theattenuation of drilling fluid pulse in multiphase flow restrictsthe use of down hole measuring devices with transmissionmedium of drilling fluid pulse in aerated drilling [16 17]PMWDMWDdatawere not included in the datamonitoringsystem for aerated drilling
As shown in Figures 1 and 2 the real-time data monitor-ing systems consist of various kinds measuring instrumentsan incoherent receptor a signal converser and a PC Toacquire various parameters in different types in real time themeasuring facilities used here include pressure transducerstemperature transducer gas and liquid flowmeters densitymeasuring unit and portable gas analyzer The strong tech-nology and sophisticated equipment were applied in dataacquisitions in this paperThe pressure transducers used herehave a frequency response of 01sim1000Hz and a maximumfull scale output error of 075 FSO over the 0 to 70∘Ccompensated rangeThe injection and outlet gas temperature
was measured by the temperature transducers with widetemperature range from minus55∘C to +150∘C and excellentlinearity of plusmn03∘C In order to assure measurement accuracydifferent types of portable type clip ultrasonic flowmeter wereclamped on to the existing pipeline to acquire respectivelythe drilling fluid oil and gas rates The density measuringunit proposed by Carlsen et al [18] consisting of threepressure transducers placed along the circulating path fromthe pump to the connection to the drill string was usedto identify automatically the injection drilling fluid densityAn advantage of this method is that it enables automaticupdates of the density Likewise the outlet drilling fluiddensity can readily be determined The density of outlet oilwas measured using a common method for the reason that itis relatively fixed for a particular reservoir The acquisition ofoutlet gas component can be completed using a portable gasanalyzer One of the technical superiorities of this system isthat a digital microwave transmission technique was used totransmit the data recorded by various measuring equipmentinstead of the use of the cable All the measuring instrumentsshown in Figures 1 and 2 were attached to a wireless radiatedelement respectively Measurement signals from pressuretransducers flowmeters and other instrumentswere receivedwirelessly by an incoherent receptor and then analyzed andrecorded using a signal analyzer after being converted intodigital signals It is noted that the incoherent receptiontechnique indicated in Spalding and Middleton [19] wasapplied here to tackle the reception of signals in the impulsiveinterference environment Data acquisition software calledLabVIEW was used to capture the measurement signalsThese measurements together with compound logging dataand PMWDMWD data were preprocessed to detect neces-sary information for reservoir characterization in standarddata formats usingMATLAB on a personal computer Owingto the use of wireless transmission technique the signalreceptor and data processing system no longer have to belocated near the well site which makes remote supervisoryand technical service possible The work above in this paperensures that the data are accurate real time and easilyavailable which is critical and considerable for reservoircharacterization during drilling
3 Transient Wellbore Flow Model
The wellbore transients have significant effect on actualwell inflow and therefore should be considered in reservoircharacterization The real-time data monitoring system canprovide bottom hole pressure in liquid-based underbalanceddrilling During aerated drilling the wellbore transientsmust be calculated by mathematical means owing to theserious attenuation of PMWD signals In this section a one-dimensional liquid-gas two-phase transient model governingwellbore flow with thermal effects in aerated drilling isdeveloped with variables resolved in the axial direction onlyBesides the effect of the cutting bed in horizontal sections isconsidered Owing to complexity of the liquid-gas two-phaseflow transient in wellbore the following assumptions madefor the model development are primarily given
4 Journal of Applied Mathematics
Choke manifold Combustion cell
Three-wayvalve
ThrottleMud pumps
BlenderThrottle
Portable gasanalyzer
Liquidflowmeter
Liquid flowmeterShale
shakers
Pressure transducer
Reserve pit
Mud pits
Pressuretransducer
Sampling
Booster
PC Reservoir characterization Compound logging data
Oil skimming tank
11
Sampling
Signal converser Incoherent receptor
Density measuring unit
Temperature transducer
Pressure transducer
Signal analyzer
Outlet (oil)
Pressure transducer
Gas flowmeter
Density measuring
unit
Throttle
Separator
Liquid flowmeter
Gas flowmeter
Injection (mud)
Drillstrings
Annulus
Injection(gas)
Injection(mixture)
Outlet
Outlet (mud)
Outlet (gas)
Outlet (mud)
Primary flow line
RBOP
Secondaryflow line
Nitrogengenerator
Compressor
Atmosphere
Solids disposal
Mud return line
Temperature transducer
deg100
50
minus0
minus10mV
Figure 1 A schematic of the placement of the real-time data monitoring system for aerated drilling
deg
Choke manifold Combustion cell
Three-wayvalve
ThrottleMud pumps Portable gas
analyzer
Liquidflowmeter
Liquid flowmeterShale
shakers
Pressure transducer
Reserve pit
Mud pits
Pressuretransducer
Sampling
100
50
PC Reservoir characterization Compound logging data
Oil skimming tank
11
Sampling
Signal converser Incoherent receptor
Density measuring unit
Pressure transducer
Signal analyzer
Outlet (oil)
Density measuring
unit
Throttle
Separator
Liquid flowmeter
Gas flowmeter
Injection (mud)
Injection (mud)
Mud return line Drillstrings
Annulus
Outlet
Outlet (mud)
Outlet (gas)
Outlet (mud)
Temperature transducer Primary flow line
RBOP
Secondaryflow line
Solids disposal
minus0
minus10mV
Figure 2 A schematic of the placement of the real-time data monitoring system for liquid-based underbalanced drilling
(i) The liquid phase fluids are incompressible and New-tonian
(ii) Properties of fluids are uniform and constant
(iii) The bubbles are spherical in shape having diameter asthe characteristic
(iv) The transverse lift force is neglected
(v) The turbulent dispersion force of gas phase is neglec-ted
(vi) The effects of breakup and coalescence of droplets andbubbles are neglected
(vii) Mass transfer effects are neglected
31 Model Development In this paper a transient model ofliquid-gas two-phase flow in wellbore is proposed on thebasis of the three-dimensional model averaged in time andspace given by Lahey andDrew [20]The governing equationsconsist of continuity equations for each component and a
Journal of Applied Mathematics 5
momentum conservation equation Such equations can bewritten as follows
gas continuity equation
120597 (120588
119892120572
119892)
120597119905
+
120597 (120588
119892120572
119892119906
119892)
120597119911
= 0
(1)
liquid continuity equation
120597 (120588
119897120572
119897)
120597119905
+
120597 (120588
119897120572
119897119906
119897)
120597119911
= 0(2)
gas momentum conservation equation
120597 (120588
119892120572
119892119906
119892)
120597119905
+
120597 (120588
119892120572
119892119906
2
119892
)
120597119911
+ 120572
119892
120597119901
120597119911
= minus120572
119892120588
119892119892 sin 120579 minus 119865
119889119892minus 119865V119898 minus 119865
119908119892
(3)
liquid momentum conservation equation
120597 (120588
119897120572
119897119906
119897)
120597119905
+
120597 (120588
119897120572
119897119906
2
119897
)
120597119911
+ 120572
119897
120597119901
120597119911
= minus120572
119897120588
119897119892 sin 120579 minus 119865
119889119892minus 119865V119898 minus 119865
119908119897
(4)
where 119901 is pressure 119892 is the acceleration due to gravity 120588is density 119906 is velocity 120572 is the volumetric fraction 120579 is thedeviation angle 119905 and 119911 are temporal and spatial coordi-nates 119865
119889is drag force 119865V119898 is virtual mass force 119865
119908is
wall shear force and the subscripts 119892 119897 represent gas andliquid respectively The indispensable closure relationshipsappearing in equations above are formulated and describedin Appendix A
Due to the mixture of gas-liquid two phases the dis-tribution relation of two-phase homogeneous fluid can benormalized as
120572
119892+ 120572
119897= 1 (5)
In this paper gas phase can be deemed as the ideal gas andcan be evaluated using the equation of state in the followingmanner
119901 = 119885120588
119892119877119879 (6)
where 119879 is temperature 119877 denotes the gas constant and 119885 isthe real gas deviation factor which is the function of pressuretemperature and the nature of the gas
In the transient liquid-gas two-phase flow model theheat transfer between wellbore and formation is consideredby introducing a wellbore heat transfer model during two-phase flow presented by Hasan and Kabir [21] based on arigorous energy balance equation for two-phase flow [22] Anexpression for fluid temperature in wellbore as a function ofwell depth and producing time is primarily given by
119879 = 119879
119890119894+ 120585 [1 minus 119890
119867120585
] (
119892
119892
119888
sin 120579
119869119862
119901
+ 120593 + 119892
119879sin 120579)
+ 119890
(119867minus119911)120585
(119879
119891119887ℎminus 119879
119890119887ℎ)
(7)
where 119879
119890119894is undisturbed formation temperature at given
depth 120585 is inverse relaxation distance 119867 is total welldepth from surface 119892
119888and 119869 represent conversion factors
119862
119901is the mean heat capacity of the multiphase fluid at
constant pressure 119892119879is geothermal temperature gradient
120593 is parameter combining the Joule-Thompson and kineticenergy effects 119879
119891119887ℎis fluid temperature at the bottom hole
and 119879
119890119887ℎis formation temperature at bottom hole Some
important parameters are discussed in detail in Appendix BIn the transient wellbore flow model we consider the
density behavior of drilling fluid under high pressure andhigh temperature conditions during underbalanced drillingoperation A more accurate analytical model for density-pressure-temperature dependence for drilling fluid in drillingproposed by Karstad and Aadnoy [23] was presented in thefollowing manner
120588
119897= 120588
119897119904119891119890
120574119901(119901minus119901119904119891)+120574119901119901(119901minus119901119904119891)2+120574119879(119879minus119879119904119891)+120574119879119879(119879minus119879119904119891)
2+120574119901119879(119901minus119901119904119891)(119879minus119879119904119891)
(8)
where 120588
119897119904119891is the drilling fluid density under standard con-
ditions 119879119904119891
is the standard temperature 120588119904119891
is the standardpressure and the values of 120574
119901 120574
119901119901 120574
119879 120574
119879119879 and 120574
119901119879are
essentially unknown and must be determined for differentmuds from density measurements at elevated pressures andtemperatures
Though we have made an assumption of gas liquid two-phase flow in wellbore the effect of cutting bed in horizontalwell on wellbore flow simulation has to be considered Thecutting bed existing in the horizontal annulus reduces theopen flow area of gas liquid two-phase fluid which is acritical factor in wellbore flow simulation In this paper weconsider the effect of cutting bed by evaluating the open flow
area of gas liquid two-phase fluid in horizontal annuluscausing the movement of cutting bed The cuttings trans-port in horizontal wellbore has been investigated by manyresearchers [24ndash30] In this paper we use a mechanics modelwith aerated drilling fluid proposed by Zhou [30] to predictthe movement of cutting bed and the cutting bed height
32 Numerical Solution In order to solve the model thefinite difference technique which is one of the most widelyused numerical methods is applied in this paper Thetechnique is implemented by replacing all derivatives bydifference quotients Owing to the introduction of analyticalexpression of temperature the model is easier to solve using
6 Journal of Applied Mathematics
the technique Discretization of governing equations can beobtained applying a first order downstream implicit schemefor time derivations For the stability of numerical solutionsthe donor cell concept is used The fluid exit conditions areassumed to be the same as the fluid conditions in the nodeitself The discretized form of governing equations can bewritten in the following matrix form
D119895(k0119895
) k119905+Δ119905119895
= E119895(k0119895
k119905119895
k119905+Δ119905119895minus1
) (9)
whereD is the coefficient matrix E is the independent vector119895 is cell number the superscripts 119905 and 119905+Δ119905 are the dependentvariables calculated at the old and new times respectively thesuperscript 0 represents the dummy variables for the iterativemethod and v is a column vector of dependent variablesgiven as follows
v = (119901 120572
119892 119906
119892 119906
119897)
119879
(10)
where the superscript 119879 indicates the transposeMechanistic models for two-phase flow in drill string and
annuli [31ndash33] are used to provide the necessary informationfor numerical calculation about flow patterns pressure dropsphase volumetric fractions and phase velocities in each oldtime node The wellbore fluid temperature at each grid pointcan be estimated using (7) In this paper we use the algorithmbased on the factorization of a matrix using a version of theGaussian elimination with partial pivoting
It is important to note that the numerical solution istransient due to the fact that almost all the transient termsare considered in our model In addition the numericalsolution of two-phase wellbore flow under constantly chang-ing flowing environmental can be given easily owing to theestablishment of real-time data monitoring system
4 Transient Well Influx Model
In underbalanced drilling the transient well influx can bedeemed as a complex well test The complexity arises fromthe fact that the boundary conditions vary with times invalue and type during the test because the well is con-tinuously increasing in length In the drilled part of thereservoir we have a Dirichlet boundary condition Insteadthe Neumann boundary condition is dealt with along thefuture well trajectory in the reservoir Also keep in mindthat the transient influx rates are influenced by variation inunderbalance and penetration rateTherefore the traditionalwell test techniques are not fit for the purpose of modelingtransient well influx during underbalanced drilling Becauseof the complexity of the problems a realistic model is neededto predict the transient well inflow while drilling
41 Mathematical Model Themodel in this paper representsa simplification of the actual reservoir It is assumed thatthe reservoir is symmetric around the well and possessesconstant reservoir and parameters During the transientperiod we assume that there is no pressure response from theborder of the reservoir For transient flow of a single phase
the governing differential equation can be given in the formof diffusivity equation
nabla
2
119901 =
120601120583119888
119896
120597119901
120597119905
(11)
where 120601 is porosity 119888 is reservoir compressibility 120583 is theviscosity of reservoir fluid and 119896 is the reservoir permeability
With the above assumption that there is no pressureresponse from the border of the reservoir the outer boundaryis given in the following Neumann manner
120597119901
120597119899
= 0(12)
where 119899 is the normal of the boundary surfacesEssentially the main difference of transient influx during
drilling with convention well test operations lies in the innerboundary which changes with time For the part of thereservoir penetrated by a horizontal well we have a Dirichletboundary condition
119901 = 119901
119908ℎ (13)
where 119901119908ℎ
is the pressure at bottom holeFor the undisturbed part of the reservoir the influx rates
are zero in other words the inner boundary conditionslikewise can be captured by the above Neumannmanner It isimportant to note that as a result of the continuous increasein well length the inner boundary conditions do not onlychange in value but in types as well Every drill step the partof the reservoir that is dominated by the Neumann conditiondecreases while the zone governed by theDirichlet conditionincreases This means that we have to deal with a new set ofequations with different boundary conditions for every stepdrill stepThus we are in dire need of new realistic expressionto describe the transient well influx during underbalanceddrilling
42 Approximate Analytical Solution To allow analyticalsolutions of the transient influx problem some essentialhypotheses are made in this paper We assume that thereservoir consists of a number of independent elements orzones as shown in Figure 3 It is assumed that the fluidflows along planes perpendicular to the well During under-balanced drilling a new zone is added to the well everystep in time The size of the time step and the thickness ofdrilled zones must conform to the penetration rate which isconsidered to be constant here It is assumed that productionfrom new added zone starts at the moment when it is beingpenetrated by drilling The total production rate at a giventime can be obtained by adding the production response ofindividual zones that time Thus the total production rate asa function of time can be given by
119902
119905119900119905(119905) = int
119911(119905)
0
119902
119908(119911 119905) 119889119911
(14)
Journal of Applied Mathematics 7
InjectionOutlet
Undisturbedreservoir
Opened reservoir elements
Permeability k1 k2 k3 k4
k1 k2 k3 k4
Figure 3 A schematic of a horizontal well drill into the reservoirconsists of a number of independent elements
where depth 119911 is a function of time 119905 and the penetrationrate 119906
119901 and 119902
119908(119909 119905) is the well influx from a unit thickness
Substitution of 119889119911 = 119906
119901119889119905 yields
119902
119905119900119905(119905) = int
119905
0
119902
119908(119911 120591) 119906
119901119889120591 (15)
Using Duhamelrsquos theorem van Kruijisdijk and Cox [6]proposed that the transient well influx for a given elementcan be rendered to a convolution of the underbalance andthe time derivative of the well influx for a constant andunit underbalance and rewrote the above equation in thefollowing manners
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (119901
119903119890119904minus 119901
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(16)
where 119902
119908119906(119905) denotes the unit-underbalanced inflow of unit
reservoir segment at the given time Θ represents the setof reservoir parameters that define the flow geometry andproperties 119901
119903119890119904is the reservoir pore pressure and 119901
119908is a
function of time and is defined as
119901
119908(119905) =
119901
119903119890119904for 119905 le 119905open (119911)
119901
119908ℎ(119905) for 119905 gt 119905open (119911)
(17)
The function 119905open(119911) represents the time atwhich the drillbit penetrates point 119911 thereby opening that point along thewell trajectory up to flow
To obtain an analytical solution of transient well inflowat any given time we need a realistic expression of the unit-underbalance transient inflow of each unit thickness segment119902
119908119906(119905) Based on the appropriate source functions in Laplace
space van Kruijisdijik [34] proposed the following analyticalsolution
119902
119908119906(119905) =
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(18)
where ℎ is the reservoir thickness 119903119908is the radius of the
wellbore119861119900is the volume factor of the reservoir fluid 119878
119911is the
effective skin due to vertical flow 1198861and 119886
2are the coefficient
and have respectively the values of 0611 and 1083 in the earlytime of transient influx
For gas reservoir the expression of the transient inflowis a bit different from (16) the analytical solution for oilreservoir proposed by van Kruijisdijk and Cox [6] Thecompressibility of gas decides the influx difference betweenoil and gas reservoirWe define the pseudopressure as follows
= 2int
119901
1199010
119901
120583
119892(119901)119885 (119901)
119889119901 (19)
where 119901
0is the known pressure for reference 120583
119892is the gas
viscosity and 119885 is the compressibility factor of the gas Thenthe total influx rates of gas reservoir during underbalanceddrilling can be given
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (
119903119890119904minus
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(20)
Analogously we rewrite the analytical expression of 119902119908119906
forgas reservoir in the following manner
119902
119908119906(119905) =
120587119896ℎ
119861
119892
119885
119904119888119879
119904119888120588
119892119904119888
119901
119904119888119879
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(21)
where the subscript denotes the standard state
5 Methodology of EstimatingReservoir Characterization
After establishing datamonitoring system in real time a tran-sient liquid-gas two-phase flow model in wellbore and wellinflux model during drilling have been derived Hereuntowe have reliable data acquisition approach and theoreticalmodel for reservoir characterization In this section let usfocus on specific approach to estimate reservoir properties Atfirst we will propose a new methodology to acquire reservoirpore pressure and then discuss how to extract the reservoirpermeability profiles during drilling
51 Reservoir Pore Pressure Inspired by the interestingmethodology of identifying reservoir pore pressure proposedby Kneissl [12] a new improved method of testing reservoirpore pressure is developed using different testing procedureavoiding the uncertainties affected by variations of fluid flowbehavior in the annulus sections and unpredictable inflowof new added zones It is noted that the idea of identifyingreservoir pore pressure by actively fluctuating the bottomhole pressure is still the key kernel thought of our methodFocusing on the new methodology a principal assumptionhas to be made that the reservoir drilled consists of differentzones with constant formation pressure coefficient whichcorresponds with the most common circumstances Withthe continuous pressure system assumption it is easy to
8 Journal of Applied Mathematics
obtain reservoir pore pressure of each zone by extracting thereservoir pressure coefficient when the reservoir is openedThis greatly simplifies the procedure of pore pressure testand avoids complex mathematical computation usually usedin other methods To eliminate the uncertainties of estimateresults introduced by continuous inflow of new zones it isneeded to stop drilling but keep circulation to begin thetesting operation when the first reservoir zone was openedwhich is the difference from Kneisslrsquos method in testingprocedure Taking into account the fact that only the first zonewas opened in the testing operation the transient inflow ofwell can be given by
119902
119908(119905) =
2120587119896ℎ (119901
119903119890119904minus 119901
119908(119905))
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(22)
It can be rewritten as
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(23)
At very short time the expression reduces to the followingmanner
lim119905rarr0
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
= lim119905rarr0
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911
(24)
which is entirely independent of the time and the downside of the equation can be considered constant for a givenreservoir It also can be interpreted that the transient inflowof well has a significant negative linear correlation with thepressure at bottom hole in the earliest hours of inflow Forthe inflow of well to become zero the reservoir pore pressureis approached by the pressure at bottom hole Thence wecan identify the reservoir pore pressure by searching forthe linear correlation between the inflow and pressure atbottom at the early stage of transient inflow This processis performed by introducing artificially fluctuations in thebottom hole pressure and by measuring the inflow rates andbottom hole pressure based on the real-time data monitoringsystem For aerated drilling the bottom hole pressure can beestimated using the transient wellbore flowmodel mentionedin this paper Figure 4 illustrates some details concerninghow to extract the reservoir pore pressure Here linear fittingof some measurement points is used to identify the linearcorrelation between thewell inflow and bottomhole pressureand the reservoir pore pressure can be read at the crossingof the best-fit regression line and the horizontal axis Forthe reliability of test results the number of testing pointsshould not be less than three Fluctuations of the bottom holepressure can be introduced by managing the choke valvechanging gas injection rates or pump rates To eliminatethe effects of variations of fluid flow in the wellbore onthe estimated results it is necessary to leave enough timeto capture relative steady inflow rates for each fluctuating
High
High
Low
0
qw
pw
Testing dataBest-fit regression line
Reservoir pressure
Figure 4 Reservoir pore pressure test by introducing fluctuation atthe bottom hole pressure
operation and the time needed lasts for a few minutes ormore than one hour which depends on well depth the typeof operations introducing the fluctuation in the bottom holepressure reservoir characteristics such as permeability andformation fluid properties and so on
Having acquired the reservoir pore pressure of the firstzone when the reservoir is opened the reservoir pressurecoefficient and pressure of subsequent zones can be obtainedduring drilling using a simple formula For the case wheremore than one reservoir with different pressure system wasdrilled new testing procedure should be repeated when newreservoir was opened The only difference is that the inflowmeasurements consist of the transient inflow response ofthe former reservoir and the transient well inflow of newreservoirrsquos first zone Here necessarymathematical treatmentof the inflow measurements is needed
52 Permeability Profiles To determine the reservoir perme-ability we make the simplifying assumption that the perme-ability is constant in specified zones of the well Transientinflux from each reservoir zone with different permeabilityat the time of interest constitutes the total production rates ofthewell which can be got from the real-time data acquisitionssystem The analytical expressions of total production ratesand unit-underbalance response of each zone which arerelated to the permeability have been established in the lastsection of this paper The reservoir pore pressure of eachreservoir zone can be calculated after testing the reservoirpressure coefficient just when the reservoir was opened Itis assumed that the porosity reservoir height and otherreservoir parameters apart from permeability are constantand known Theoretically the permeability of each reservoirzone can be easily determined using (18) and (21) Unfor-tunately the analytical expressions of the total productionrates are given in integral form which results in that theycannot readily be implemented in spreadsheet and calculator
Journal of Applied Mathematics 9
applications To facilitate the calculation a full discretizationof the total production rates formula is given instead of theintegral form in the following manner
119902
119905119900119905(119905) = 119906
119901(119901
119903119890119904minus 119901
119908)
119899=119905Δ119905
sum
119894=1
119902
119908119906119894(Θ
119894 119905 minus 119905
119894) Δ119905 (25)
where Δ119905 represents the time needed to penetrate througha reservoir element which is constant with the assumptionof the fixed penetration rate 119902
119908119906119894(Θ
119894 119905 minus 119905
119894) denotes unit-
underbalanced inflow of unit reservoir segment from zone 119894and 119905
119894denotes the time the wellbore reaches zone 119894 The value
of 119902119908119906119894
(Θ
119894 119905 minus 119905
119894) for nonpositive arguments is set equal to 0
The above discretization equation was given on the basisof a reasonable assumption that we have a constant underbal-ance which is realistic and is of engineering significance forunderbalanced drilling of a horizontal well
First we discuss how to extract the permeability of the1st reservoir zone The total production rates from the real-time monitoring system at the first time step when reservoiris opened can be simply considered to be the influx from thefirst zone Then we have the following formula
119902
119905119900119905(119905
1) = 119902
1199081(119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) 119902
1199081199061(Θ
1 119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
1ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896Δ119905120601120583119888119903
2
119908
(26)
Solving the equation above 1198961 the permeability of the 1st
reservoir zone can be given as follows
119896
1= (119898
2119902
1199081(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
1199081
(119905
1) Δ119905 +
119902
1199081(119905
1) 119878
119911
119898
1
)
2
(27)
where
119898
1=
2119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) ℎ119886
1
120583119861
119900119903
119908
119898
2=
119886
2
2119898
1119903
119908
radic120601120583119888
(28)
Analogously well influx from the reservoir element 119894 canbe given
119902
119908119894(119905
1)
= 119902
119905119900119905(119905
119894) minus
119894minus1
sum
119899=1
119902
119908119899(119905
119894minus119899)
= 119902
119905119900119905(119905
119894) minus 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
119894minus1
sum
119899=1
119902
119908119906119899(119905
119894minus 119905
119899)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
119894ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896
119894Δ119905120601120583119888119903
2
119908
(29)
where 119902tot(119905119894) represents the total production rates of the wellat time 119905
119894when the reservoir element is opened 119902
119908119906119899(119905
119894minus 119905
119899)
denotes the unit-underbalance transient influx response ofunit thickness reservoir from reservoir zone 119899 at time 119905
119894and
can be given using (21)Then we can extract the permeability of the reservoir
zone 119894 by
119896
119894= (119898
2119902
119908119894(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
119908119894
(119905
1) Δ119905 +
119902
119908119894(119905
1) 119878
119911
119898
1
)
2
(30)
Using the methodology the permeability of a set ofreservoir zones can be successively extracted as the reservoiris being penetrated by a horizontal well To facilitate theprecise calculation and estimate permeability profiles in timea computer procedure was used in this paper The success ofreservoir permeability estimation profits from reliable real-time data monitoring system advanced wellbore flow andreservoir model and an innovative reservoir pore pressuretest approach
6 Results and Discussion
The methodology presented in this paper has been used toidentify the reservoir pore pressure and permeability profilesof approximately 10 wells during underbalanced drilling inChina In order to illustrate the above approach in detail anactual horizontal well and gas reservoir are considered in thissection It is appropriate to emphasize that the well picked ascase study is the first successful application of this method-ology More exhaustive data and offset information from thiswell facilitate the effectiveness evaluation of this methodThereservoir dealt with here is the Ordovician carbonate gasreservoir with natural fractures as the dominant gas storagespaces and flowing channels To avoid lost circulation andformation damage the well is drilled underbalanced usingthe aerated clay-free drilling fluid while this is also beneficialfor well control Here nitrogen is used as the injection gasThe hole geometry and drilling assembly of this well wereillustrated in Figure 5 Some basic parameters for reservoirand drilling fluid used in reservoir characterization wereshown in Table 1
61 Data Acquisition in Real Time The real-time data mon-itoring system for aerated drilling presented in this paperwas used to acquire basic data for reservoir characterizationin real time The application of this system guaranteesthat the indispensable parameters are accurate and timelywhichmakes it possible to identify reservoir characterizationDuring drilling this system succeed in the integration of thedata from compound logging and our sensitive measuringinstruments and the digital microwave transmission wasproved to be realizable and reliable to deliver wirelesslydata Some typical acquired measurements plotted againsttime are shown in Figures 6ndash10 In order to illustrate thetransient behavior for different parameters the measuringtime for different parameters in figures differs The standpipe
10 Journal of Applied Mathematics
Drill bit
Cement
Casing
Drill strings
Wellhead
Bottom holeBarefoot interval
Annulus
Protective casing interval
Drill strings size
Diameter 01524m
Diameter 01524mDepth 4000ndash4960m
Inner diameter 022m
Outside diameter 01397mInner diameter 01214m
Outside diameter 00889mInner diameter 00702m
Outside diameter 00889mInner diameter 00381m
Depth 0ndash
Depth 0ndash1800m
Depth 1800ndash4930m
Depth 4930ndash4960m
4000m
Figure 5 The hole geometry and drilling assembly of the well
Table 1 Basic parameters for reservoir and drilling fluid used inreservoir characterization
Depth evaluation of the reservoir m 4156Reservoir thickness m 15Porosity 12Reservoir fluid volume factor m3stdm3 0008Reservoir fluid viscosity mPasdots 0035Reservoir compressibility Paminus1 116 times 10minus9
Reservoir fluid compressibility Paminus1 1177 times 10minus9
Geothermal temperature Ksdotmminus1 003Drilling fluid density at standard conditions gsdotcmminus3 104Drilling fluid viscosity at standard conditions mPasdots 20Injection gas specific gravity 1 097Injection gas viscosity at standard conditions mPasdots 0019
pressure and casing pressure for different time are plottedrespectively in Figures 6 and 7 It can be seen that thetransient fluctuations of standpipe pressure are more acutethan that of casing pressure In general this difference canbe aroused by unsteady drilling fluid and gas injection checkcalve measuring apparatus installed along drill string anddrill string vibrationThe casing pressure changing with timein Figure 7 indicates the different outlet gas rates or variedchoke opening Figure 8 shows the drilling fluid density asa function of time for outlet and injection respectivelyContrary to the standard drilling operations more accurateand automatic measurements of drilling fluid density can beobtained in real time utilizing instrumented standpipe andseparator drilling fluid outlet pipe using different pressure
2030 2118 2207 2254 234110
11
12
13
14
15
16
17
18
Stan
dpip
e pre
ssur
e (M
Pa)
Time1930
Figure 6 Data acquisitionmdashstandpipe pressure data versus time(2010-9-27)
1151 1342 1527 1715 1901 2052 2230250
275
300
325
350
375
400Ca
sing
pres
sure
(MPa
)
Time1000
Figure 7 Data acquisitionmdashcasing pressure data versus time (2010-9-27)
transducers not measured manually in intervals of 15 min-utes It is noted that the outlet drilling fluid density is slightlylower than that of injection fluid and fluctuates wildly Thistransient behavior of outlet drilling fluid density occurs as aresult of varied outlet gas rates and nonthorough degassing ofdrilling fluid In this study we monitor the total hydrocarboncontent of outlet gas and outlet gas rates to acquire thereservoir gas inflow rates in real timeThemeasured outlet gasrates and reservoir gas inflow rates are presented in Figure 9The real-time reservoir gas inflow rates absolutely criticalfor reservoir characterization are calculated using the outletgas rates and total hydrocarbon content in time of interestas shown in Figure 10 In sum the application of the newreal-time data monitoring system in this well helps drillingcontractor with good underbalanced drilling operations and
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
Journal of Applied Mathematics 3
optimization in underbalanced operations The measure-ments of interest here are as follows
(i) injection and outlet drilling fluid densities(ii) injection and outlet drilling fluid rates(iii) drilling fluid viscosity(iv) oil outlet rates and density(v) penetration rate in the formation(vi) injection and outlet gas rates pressure and tempera-
ture(vii) outlet gas component(viii) standpipe and surface casing pressure(ix) bottom hole pressure(x) measured depth and wellbore diameter(xi) BHA and hole trajectory(xii) formation porosity
Schematics of the location of the real-time data moni-toring system with respect to the well for aerated drillingand liquid-based underbalanced drilling are illustrated inFigures 1 and 2 respectively In order to explain the datamonitoring systems clearly it is necessary to first introducethe circulation process for underbalanced drilling Duringaerated drilling operations drilling fluid from mud pits andnitrogen from gas injection system consisting of compressornitrogen generator and booster are mixed and injected intothe drill strings under pressure via a fluid line as shown inFigure 1 The gasified drilling fluid is then circulated out withthe produced formation fluid through the annulus into theprimary flow line and enters the separator where gas and oilare separated The drilling fluid returns to the mud pits viaa return line after taking out the solids using shale shakersProduced oil is sent to an oil shimming tank Separated gasis sent to a combustion cell For liquid-based underbalanceddrilling the circulation process is somewhat different becauseonly drilling fluid is injected as shown in Figure 2 Thusthe measurements of the gas injection rates pressure andtemperature were not involved in the data monitoring systemfor liquid-based unbalanced drilling For the reason that theattenuation of drilling fluid pulse in multiphase flow restrictsthe use of down hole measuring devices with transmissionmedium of drilling fluid pulse in aerated drilling [16 17]PMWDMWDdatawere not included in the datamonitoringsystem for aerated drilling
As shown in Figures 1 and 2 the real-time data monitor-ing systems consist of various kinds measuring instrumentsan incoherent receptor a signal converser and a PC Toacquire various parameters in different types in real time themeasuring facilities used here include pressure transducerstemperature transducer gas and liquid flowmeters densitymeasuring unit and portable gas analyzer The strong tech-nology and sophisticated equipment were applied in dataacquisitions in this paperThe pressure transducers used herehave a frequency response of 01sim1000Hz and a maximumfull scale output error of 075 FSO over the 0 to 70∘Ccompensated rangeThe injection and outlet gas temperature
was measured by the temperature transducers with widetemperature range from minus55∘C to +150∘C and excellentlinearity of plusmn03∘C In order to assure measurement accuracydifferent types of portable type clip ultrasonic flowmeter wereclamped on to the existing pipeline to acquire respectivelythe drilling fluid oil and gas rates The density measuringunit proposed by Carlsen et al [18] consisting of threepressure transducers placed along the circulating path fromthe pump to the connection to the drill string was usedto identify automatically the injection drilling fluid densityAn advantage of this method is that it enables automaticupdates of the density Likewise the outlet drilling fluiddensity can readily be determined The density of outlet oilwas measured using a common method for the reason that itis relatively fixed for a particular reservoir The acquisition ofoutlet gas component can be completed using a portable gasanalyzer One of the technical superiorities of this system isthat a digital microwave transmission technique was used totransmit the data recorded by various measuring equipmentinstead of the use of the cable All the measuring instrumentsshown in Figures 1 and 2 were attached to a wireless radiatedelement respectively Measurement signals from pressuretransducers flowmeters and other instrumentswere receivedwirelessly by an incoherent receptor and then analyzed andrecorded using a signal analyzer after being converted intodigital signals It is noted that the incoherent receptiontechnique indicated in Spalding and Middleton [19] wasapplied here to tackle the reception of signals in the impulsiveinterference environment Data acquisition software calledLabVIEW was used to capture the measurement signalsThese measurements together with compound logging dataand PMWDMWD data were preprocessed to detect neces-sary information for reservoir characterization in standarddata formats usingMATLAB on a personal computer Owingto the use of wireless transmission technique the signalreceptor and data processing system no longer have to belocated near the well site which makes remote supervisoryand technical service possible The work above in this paperensures that the data are accurate real time and easilyavailable which is critical and considerable for reservoircharacterization during drilling
3 Transient Wellbore Flow Model
The wellbore transients have significant effect on actualwell inflow and therefore should be considered in reservoircharacterization The real-time data monitoring system canprovide bottom hole pressure in liquid-based underbalanceddrilling During aerated drilling the wellbore transientsmust be calculated by mathematical means owing to theserious attenuation of PMWD signals In this section a one-dimensional liquid-gas two-phase transient model governingwellbore flow with thermal effects in aerated drilling isdeveloped with variables resolved in the axial direction onlyBesides the effect of the cutting bed in horizontal sections isconsidered Owing to complexity of the liquid-gas two-phaseflow transient in wellbore the following assumptions madefor the model development are primarily given
4 Journal of Applied Mathematics
Choke manifold Combustion cell
Three-wayvalve
ThrottleMud pumps
BlenderThrottle
Portable gasanalyzer
Liquidflowmeter
Liquid flowmeterShale
shakers
Pressure transducer
Reserve pit
Mud pits
Pressuretransducer
Sampling
Booster
PC Reservoir characterization Compound logging data
Oil skimming tank
11
Sampling
Signal converser Incoherent receptor
Density measuring unit
Temperature transducer
Pressure transducer
Signal analyzer
Outlet (oil)
Pressure transducer
Gas flowmeter
Density measuring
unit
Throttle
Separator
Liquid flowmeter
Gas flowmeter
Injection (mud)
Drillstrings
Annulus
Injection(gas)
Injection(mixture)
Outlet
Outlet (mud)
Outlet (gas)
Outlet (mud)
Primary flow line
RBOP
Secondaryflow line
Nitrogengenerator
Compressor
Atmosphere
Solids disposal
Mud return line
Temperature transducer
deg100
50
minus0
minus10mV
Figure 1 A schematic of the placement of the real-time data monitoring system for aerated drilling
deg
Choke manifold Combustion cell
Three-wayvalve
ThrottleMud pumps Portable gas
analyzer
Liquidflowmeter
Liquid flowmeterShale
shakers
Pressure transducer
Reserve pit
Mud pits
Pressuretransducer
Sampling
100
50
PC Reservoir characterization Compound logging data
Oil skimming tank
11
Sampling
Signal converser Incoherent receptor
Density measuring unit
Pressure transducer
Signal analyzer
Outlet (oil)
Density measuring
unit
Throttle
Separator
Liquid flowmeter
Gas flowmeter
Injection (mud)
Injection (mud)
Mud return line Drillstrings
Annulus
Outlet
Outlet (mud)
Outlet (gas)
Outlet (mud)
Temperature transducer Primary flow line
RBOP
Secondaryflow line
Solids disposal
minus0
minus10mV
Figure 2 A schematic of the placement of the real-time data monitoring system for liquid-based underbalanced drilling
(i) The liquid phase fluids are incompressible and New-tonian
(ii) Properties of fluids are uniform and constant
(iii) The bubbles are spherical in shape having diameter asthe characteristic
(iv) The transverse lift force is neglected
(v) The turbulent dispersion force of gas phase is neglec-ted
(vi) The effects of breakup and coalescence of droplets andbubbles are neglected
(vii) Mass transfer effects are neglected
31 Model Development In this paper a transient model ofliquid-gas two-phase flow in wellbore is proposed on thebasis of the three-dimensional model averaged in time andspace given by Lahey andDrew [20]The governing equationsconsist of continuity equations for each component and a
Journal of Applied Mathematics 5
momentum conservation equation Such equations can bewritten as follows
gas continuity equation
120597 (120588
119892120572
119892)
120597119905
+
120597 (120588
119892120572
119892119906
119892)
120597119911
= 0
(1)
liquid continuity equation
120597 (120588
119897120572
119897)
120597119905
+
120597 (120588
119897120572
119897119906
119897)
120597119911
= 0(2)
gas momentum conservation equation
120597 (120588
119892120572
119892119906
119892)
120597119905
+
120597 (120588
119892120572
119892119906
2
119892
)
120597119911
+ 120572
119892
120597119901
120597119911
= minus120572
119892120588
119892119892 sin 120579 minus 119865
119889119892minus 119865V119898 minus 119865
119908119892
(3)
liquid momentum conservation equation
120597 (120588
119897120572
119897119906
119897)
120597119905
+
120597 (120588
119897120572
119897119906
2
119897
)
120597119911
+ 120572
119897
120597119901
120597119911
= minus120572
119897120588
119897119892 sin 120579 minus 119865
119889119892minus 119865V119898 minus 119865
119908119897
(4)
where 119901 is pressure 119892 is the acceleration due to gravity 120588is density 119906 is velocity 120572 is the volumetric fraction 120579 is thedeviation angle 119905 and 119911 are temporal and spatial coordi-nates 119865
119889is drag force 119865V119898 is virtual mass force 119865
119908is
wall shear force and the subscripts 119892 119897 represent gas andliquid respectively The indispensable closure relationshipsappearing in equations above are formulated and describedin Appendix A
Due to the mixture of gas-liquid two phases the dis-tribution relation of two-phase homogeneous fluid can benormalized as
120572
119892+ 120572
119897= 1 (5)
In this paper gas phase can be deemed as the ideal gas andcan be evaluated using the equation of state in the followingmanner
119901 = 119885120588
119892119877119879 (6)
where 119879 is temperature 119877 denotes the gas constant and 119885 isthe real gas deviation factor which is the function of pressuretemperature and the nature of the gas
In the transient liquid-gas two-phase flow model theheat transfer between wellbore and formation is consideredby introducing a wellbore heat transfer model during two-phase flow presented by Hasan and Kabir [21] based on arigorous energy balance equation for two-phase flow [22] Anexpression for fluid temperature in wellbore as a function ofwell depth and producing time is primarily given by
119879 = 119879
119890119894+ 120585 [1 minus 119890
119867120585
] (
119892
119892
119888
sin 120579
119869119862
119901
+ 120593 + 119892
119879sin 120579)
+ 119890
(119867minus119911)120585
(119879
119891119887ℎminus 119879
119890119887ℎ)
(7)
where 119879
119890119894is undisturbed formation temperature at given
depth 120585 is inverse relaxation distance 119867 is total welldepth from surface 119892
119888and 119869 represent conversion factors
119862
119901is the mean heat capacity of the multiphase fluid at
constant pressure 119892119879is geothermal temperature gradient
120593 is parameter combining the Joule-Thompson and kineticenergy effects 119879
119891119887ℎis fluid temperature at the bottom hole
and 119879
119890119887ℎis formation temperature at bottom hole Some
important parameters are discussed in detail in Appendix BIn the transient wellbore flow model we consider the
density behavior of drilling fluid under high pressure andhigh temperature conditions during underbalanced drillingoperation A more accurate analytical model for density-pressure-temperature dependence for drilling fluid in drillingproposed by Karstad and Aadnoy [23] was presented in thefollowing manner
120588
119897= 120588
119897119904119891119890
120574119901(119901minus119901119904119891)+120574119901119901(119901minus119901119904119891)2+120574119879(119879minus119879119904119891)+120574119879119879(119879minus119879119904119891)
2+120574119901119879(119901minus119901119904119891)(119879minus119879119904119891)
(8)
where 120588
119897119904119891is the drilling fluid density under standard con-
ditions 119879119904119891
is the standard temperature 120588119904119891
is the standardpressure and the values of 120574
119901 120574
119901119901 120574
119879 120574
119879119879 and 120574
119901119879are
essentially unknown and must be determined for differentmuds from density measurements at elevated pressures andtemperatures
Though we have made an assumption of gas liquid two-phase flow in wellbore the effect of cutting bed in horizontalwell on wellbore flow simulation has to be considered Thecutting bed existing in the horizontal annulus reduces theopen flow area of gas liquid two-phase fluid which is acritical factor in wellbore flow simulation In this paper weconsider the effect of cutting bed by evaluating the open flow
area of gas liquid two-phase fluid in horizontal annuluscausing the movement of cutting bed The cuttings trans-port in horizontal wellbore has been investigated by manyresearchers [24ndash30] In this paper we use a mechanics modelwith aerated drilling fluid proposed by Zhou [30] to predictthe movement of cutting bed and the cutting bed height
32 Numerical Solution In order to solve the model thefinite difference technique which is one of the most widelyused numerical methods is applied in this paper Thetechnique is implemented by replacing all derivatives bydifference quotients Owing to the introduction of analyticalexpression of temperature the model is easier to solve using
6 Journal of Applied Mathematics
the technique Discretization of governing equations can beobtained applying a first order downstream implicit schemefor time derivations For the stability of numerical solutionsthe donor cell concept is used The fluid exit conditions areassumed to be the same as the fluid conditions in the nodeitself The discretized form of governing equations can bewritten in the following matrix form
D119895(k0119895
) k119905+Δ119905119895
= E119895(k0119895
k119905119895
k119905+Δ119905119895minus1
) (9)
whereD is the coefficient matrix E is the independent vector119895 is cell number the superscripts 119905 and 119905+Δ119905 are the dependentvariables calculated at the old and new times respectively thesuperscript 0 represents the dummy variables for the iterativemethod and v is a column vector of dependent variablesgiven as follows
v = (119901 120572
119892 119906
119892 119906
119897)
119879
(10)
where the superscript 119879 indicates the transposeMechanistic models for two-phase flow in drill string and
annuli [31ndash33] are used to provide the necessary informationfor numerical calculation about flow patterns pressure dropsphase volumetric fractions and phase velocities in each oldtime node The wellbore fluid temperature at each grid pointcan be estimated using (7) In this paper we use the algorithmbased on the factorization of a matrix using a version of theGaussian elimination with partial pivoting
It is important to note that the numerical solution istransient due to the fact that almost all the transient termsare considered in our model In addition the numericalsolution of two-phase wellbore flow under constantly chang-ing flowing environmental can be given easily owing to theestablishment of real-time data monitoring system
4 Transient Well Influx Model
In underbalanced drilling the transient well influx can bedeemed as a complex well test The complexity arises fromthe fact that the boundary conditions vary with times invalue and type during the test because the well is con-tinuously increasing in length In the drilled part of thereservoir we have a Dirichlet boundary condition Insteadthe Neumann boundary condition is dealt with along thefuture well trajectory in the reservoir Also keep in mindthat the transient influx rates are influenced by variation inunderbalance and penetration rateTherefore the traditionalwell test techniques are not fit for the purpose of modelingtransient well influx during underbalanced drilling Becauseof the complexity of the problems a realistic model is neededto predict the transient well inflow while drilling
41 Mathematical Model Themodel in this paper representsa simplification of the actual reservoir It is assumed thatthe reservoir is symmetric around the well and possessesconstant reservoir and parameters During the transientperiod we assume that there is no pressure response from theborder of the reservoir For transient flow of a single phase
the governing differential equation can be given in the formof diffusivity equation
nabla
2
119901 =
120601120583119888
119896
120597119901
120597119905
(11)
where 120601 is porosity 119888 is reservoir compressibility 120583 is theviscosity of reservoir fluid and 119896 is the reservoir permeability
With the above assumption that there is no pressureresponse from the border of the reservoir the outer boundaryis given in the following Neumann manner
120597119901
120597119899
= 0(12)
where 119899 is the normal of the boundary surfacesEssentially the main difference of transient influx during
drilling with convention well test operations lies in the innerboundary which changes with time For the part of thereservoir penetrated by a horizontal well we have a Dirichletboundary condition
119901 = 119901
119908ℎ (13)
where 119901119908ℎ
is the pressure at bottom holeFor the undisturbed part of the reservoir the influx rates
are zero in other words the inner boundary conditionslikewise can be captured by the above Neumannmanner It isimportant to note that as a result of the continuous increasein well length the inner boundary conditions do not onlychange in value but in types as well Every drill step the partof the reservoir that is dominated by the Neumann conditiondecreases while the zone governed by theDirichlet conditionincreases This means that we have to deal with a new set ofequations with different boundary conditions for every stepdrill stepThus we are in dire need of new realistic expressionto describe the transient well influx during underbalanceddrilling
42 Approximate Analytical Solution To allow analyticalsolutions of the transient influx problem some essentialhypotheses are made in this paper We assume that thereservoir consists of a number of independent elements orzones as shown in Figure 3 It is assumed that the fluidflows along planes perpendicular to the well During under-balanced drilling a new zone is added to the well everystep in time The size of the time step and the thickness ofdrilled zones must conform to the penetration rate which isconsidered to be constant here It is assumed that productionfrom new added zone starts at the moment when it is beingpenetrated by drilling The total production rate at a giventime can be obtained by adding the production response ofindividual zones that time Thus the total production rate asa function of time can be given by
119902
119905119900119905(119905) = int
119911(119905)
0
119902
119908(119911 119905) 119889119911
(14)
Journal of Applied Mathematics 7
InjectionOutlet
Undisturbedreservoir
Opened reservoir elements
Permeability k1 k2 k3 k4
k1 k2 k3 k4
Figure 3 A schematic of a horizontal well drill into the reservoirconsists of a number of independent elements
where depth 119911 is a function of time 119905 and the penetrationrate 119906
119901 and 119902
119908(119909 119905) is the well influx from a unit thickness
Substitution of 119889119911 = 119906
119901119889119905 yields
119902
119905119900119905(119905) = int
119905
0
119902
119908(119911 120591) 119906
119901119889120591 (15)
Using Duhamelrsquos theorem van Kruijisdijk and Cox [6]proposed that the transient well influx for a given elementcan be rendered to a convolution of the underbalance andthe time derivative of the well influx for a constant andunit underbalance and rewrote the above equation in thefollowing manners
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (119901
119903119890119904minus 119901
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(16)
where 119902
119908119906(119905) denotes the unit-underbalanced inflow of unit
reservoir segment at the given time Θ represents the setof reservoir parameters that define the flow geometry andproperties 119901
119903119890119904is the reservoir pore pressure and 119901
119908is a
function of time and is defined as
119901
119908(119905) =
119901
119903119890119904for 119905 le 119905open (119911)
119901
119908ℎ(119905) for 119905 gt 119905open (119911)
(17)
The function 119905open(119911) represents the time atwhich the drillbit penetrates point 119911 thereby opening that point along thewell trajectory up to flow
To obtain an analytical solution of transient well inflowat any given time we need a realistic expression of the unit-underbalance transient inflow of each unit thickness segment119902
119908119906(119905) Based on the appropriate source functions in Laplace
space van Kruijisdijik [34] proposed the following analyticalsolution
119902
119908119906(119905) =
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(18)
where ℎ is the reservoir thickness 119903119908is the radius of the
wellbore119861119900is the volume factor of the reservoir fluid 119878
119911is the
effective skin due to vertical flow 1198861and 119886
2are the coefficient
and have respectively the values of 0611 and 1083 in the earlytime of transient influx
For gas reservoir the expression of the transient inflowis a bit different from (16) the analytical solution for oilreservoir proposed by van Kruijisdijk and Cox [6] Thecompressibility of gas decides the influx difference betweenoil and gas reservoirWe define the pseudopressure as follows
= 2int
119901
1199010
119901
120583
119892(119901)119885 (119901)
119889119901 (19)
where 119901
0is the known pressure for reference 120583
119892is the gas
viscosity and 119885 is the compressibility factor of the gas Thenthe total influx rates of gas reservoir during underbalanceddrilling can be given
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (
119903119890119904minus
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(20)
Analogously we rewrite the analytical expression of 119902119908119906
forgas reservoir in the following manner
119902
119908119906(119905) =
120587119896ℎ
119861
119892
119885
119904119888119879
119904119888120588
119892119904119888
119901
119904119888119879
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(21)
where the subscript denotes the standard state
5 Methodology of EstimatingReservoir Characterization
After establishing datamonitoring system in real time a tran-sient liquid-gas two-phase flow model in wellbore and wellinflux model during drilling have been derived Hereuntowe have reliable data acquisition approach and theoreticalmodel for reservoir characterization In this section let usfocus on specific approach to estimate reservoir properties Atfirst we will propose a new methodology to acquire reservoirpore pressure and then discuss how to extract the reservoirpermeability profiles during drilling
51 Reservoir Pore Pressure Inspired by the interestingmethodology of identifying reservoir pore pressure proposedby Kneissl [12] a new improved method of testing reservoirpore pressure is developed using different testing procedureavoiding the uncertainties affected by variations of fluid flowbehavior in the annulus sections and unpredictable inflowof new added zones It is noted that the idea of identifyingreservoir pore pressure by actively fluctuating the bottomhole pressure is still the key kernel thought of our methodFocusing on the new methodology a principal assumptionhas to be made that the reservoir drilled consists of differentzones with constant formation pressure coefficient whichcorresponds with the most common circumstances Withthe continuous pressure system assumption it is easy to
8 Journal of Applied Mathematics
obtain reservoir pore pressure of each zone by extracting thereservoir pressure coefficient when the reservoir is openedThis greatly simplifies the procedure of pore pressure testand avoids complex mathematical computation usually usedin other methods To eliminate the uncertainties of estimateresults introduced by continuous inflow of new zones it isneeded to stop drilling but keep circulation to begin thetesting operation when the first reservoir zone was openedwhich is the difference from Kneisslrsquos method in testingprocedure Taking into account the fact that only the first zonewas opened in the testing operation the transient inflow ofwell can be given by
119902
119908(119905) =
2120587119896ℎ (119901
119903119890119904minus 119901
119908(119905))
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(22)
It can be rewritten as
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(23)
At very short time the expression reduces to the followingmanner
lim119905rarr0
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
= lim119905rarr0
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911
(24)
which is entirely independent of the time and the downside of the equation can be considered constant for a givenreservoir It also can be interpreted that the transient inflowof well has a significant negative linear correlation with thepressure at bottom hole in the earliest hours of inflow Forthe inflow of well to become zero the reservoir pore pressureis approached by the pressure at bottom hole Thence wecan identify the reservoir pore pressure by searching forthe linear correlation between the inflow and pressure atbottom at the early stage of transient inflow This processis performed by introducing artificially fluctuations in thebottom hole pressure and by measuring the inflow rates andbottom hole pressure based on the real-time data monitoringsystem For aerated drilling the bottom hole pressure can beestimated using the transient wellbore flowmodel mentionedin this paper Figure 4 illustrates some details concerninghow to extract the reservoir pore pressure Here linear fittingof some measurement points is used to identify the linearcorrelation between thewell inflow and bottomhole pressureand the reservoir pore pressure can be read at the crossingof the best-fit regression line and the horizontal axis Forthe reliability of test results the number of testing pointsshould not be less than three Fluctuations of the bottom holepressure can be introduced by managing the choke valvechanging gas injection rates or pump rates To eliminatethe effects of variations of fluid flow in the wellbore onthe estimated results it is necessary to leave enough timeto capture relative steady inflow rates for each fluctuating
High
High
Low
0
qw
pw
Testing dataBest-fit regression line
Reservoir pressure
Figure 4 Reservoir pore pressure test by introducing fluctuation atthe bottom hole pressure
operation and the time needed lasts for a few minutes ormore than one hour which depends on well depth the typeof operations introducing the fluctuation in the bottom holepressure reservoir characteristics such as permeability andformation fluid properties and so on
Having acquired the reservoir pore pressure of the firstzone when the reservoir is opened the reservoir pressurecoefficient and pressure of subsequent zones can be obtainedduring drilling using a simple formula For the case wheremore than one reservoir with different pressure system wasdrilled new testing procedure should be repeated when newreservoir was opened The only difference is that the inflowmeasurements consist of the transient inflow response ofthe former reservoir and the transient well inflow of newreservoirrsquos first zone Here necessarymathematical treatmentof the inflow measurements is needed
52 Permeability Profiles To determine the reservoir perme-ability we make the simplifying assumption that the perme-ability is constant in specified zones of the well Transientinflux from each reservoir zone with different permeabilityat the time of interest constitutes the total production rates ofthewell which can be got from the real-time data acquisitionssystem The analytical expressions of total production ratesand unit-underbalance response of each zone which arerelated to the permeability have been established in the lastsection of this paper The reservoir pore pressure of eachreservoir zone can be calculated after testing the reservoirpressure coefficient just when the reservoir was opened Itis assumed that the porosity reservoir height and otherreservoir parameters apart from permeability are constantand known Theoretically the permeability of each reservoirzone can be easily determined using (18) and (21) Unfor-tunately the analytical expressions of the total productionrates are given in integral form which results in that theycannot readily be implemented in spreadsheet and calculator
Journal of Applied Mathematics 9
applications To facilitate the calculation a full discretizationof the total production rates formula is given instead of theintegral form in the following manner
119902
119905119900119905(119905) = 119906
119901(119901
119903119890119904minus 119901
119908)
119899=119905Δ119905
sum
119894=1
119902
119908119906119894(Θ
119894 119905 minus 119905
119894) Δ119905 (25)
where Δ119905 represents the time needed to penetrate througha reservoir element which is constant with the assumptionof the fixed penetration rate 119902
119908119906119894(Θ
119894 119905 minus 119905
119894) denotes unit-
underbalanced inflow of unit reservoir segment from zone 119894and 119905
119894denotes the time the wellbore reaches zone 119894 The value
of 119902119908119906119894
(Θ
119894 119905 minus 119905
119894) for nonpositive arguments is set equal to 0
The above discretization equation was given on the basisof a reasonable assumption that we have a constant underbal-ance which is realistic and is of engineering significance forunderbalanced drilling of a horizontal well
First we discuss how to extract the permeability of the1st reservoir zone The total production rates from the real-time monitoring system at the first time step when reservoiris opened can be simply considered to be the influx from thefirst zone Then we have the following formula
119902
119905119900119905(119905
1) = 119902
1199081(119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) 119902
1199081199061(Θ
1 119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
1ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896Δ119905120601120583119888119903
2
119908
(26)
Solving the equation above 1198961 the permeability of the 1st
reservoir zone can be given as follows
119896
1= (119898
2119902
1199081(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
1199081
(119905
1) Δ119905 +
119902
1199081(119905
1) 119878
119911
119898
1
)
2
(27)
where
119898
1=
2119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) ℎ119886
1
120583119861
119900119903
119908
119898
2=
119886
2
2119898
1119903
119908
radic120601120583119888
(28)
Analogously well influx from the reservoir element 119894 canbe given
119902
119908119894(119905
1)
= 119902
119905119900119905(119905
119894) minus
119894minus1
sum
119899=1
119902
119908119899(119905
119894minus119899)
= 119902
119905119900119905(119905
119894) minus 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
119894minus1
sum
119899=1
119902
119908119906119899(119905
119894minus 119905
119899)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
119894ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896
119894Δ119905120601120583119888119903
2
119908
(29)
where 119902tot(119905119894) represents the total production rates of the wellat time 119905
119894when the reservoir element is opened 119902
119908119906119899(119905
119894minus 119905
119899)
denotes the unit-underbalance transient influx response ofunit thickness reservoir from reservoir zone 119899 at time 119905
119894and
can be given using (21)Then we can extract the permeability of the reservoir
zone 119894 by
119896
119894= (119898
2119902
119908119894(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
119908119894
(119905
1) Δ119905 +
119902
119908119894(119905
1) 119878
119911
119898
1
)
2
(30)
Using the methodology the permeability of a set ofreservoir zones can be successively extracted as the reservoiris being penetrated by a horizontal well To facilitate theprecise calculation and estimate permeability profiles in timea computer procedure was used in this paper The success ofreservoir permeability estimation profits from reliable real-time data monitoring system advanced wellbore flow andreservoir model and an innovative reservoir pore pressuretest approach
6 Results and Discussion
The methodology presented in this paper has been used toidentify the reservoir pore pressure and permeability profilesof approximately 10 wells during underbalanced drilling inChina In order to illustrate the above approach in detail anactual horizontal well and gas reservoir are considered in thissection It is appropriate to emphasize that the well picked ascase study is the first successful application of this method-ology More exhaustive data and offset information from thiswell facilitate the effectiveness evaluation of this methodThereservoir dealt with here is the Ordovician carbonate gasreservoir with natural fractures as the dominant gas storagespaces and flowing channels To avoid lost circulation andformation damage the well is drilled underbalanced usingthe aerated clay-free drilling fluid while this is also beneficialfor well control Here nitrogen is used as the injection gasThe hole geometry and drilling assembly of this well wereillustrated in Figure 5 Some basic parameters for reservoirand drilling fluid used in reservoir characterization wereshown in Table 1
61 Data Acquisition in Real Time The real-time data mon-itoring system for aerated drilling presented in this paperwas used to acquire basic data for reservoir characterizationin real time The application of this system guaranteesthat the indispensable parameters are accurate and timelywhichmakes it possible to identify reservoir characterizationDuring drilling this system succeed in the integration of thedata from compound logging and our sensitive measuringinstruments and the digital microwave transmission wasproved to be realizable and reliable to deliver wirelesslydata Some typical acquired measurements plotted againsttime are shown in Figures 6ndash10 In order to illustrate thetransient behavior for different parameters the measuringtime for different parameters in figures differs The standpipe
10 Journal of Applied Mathematics
Drill bit
Cement
Casing
Drill strings
Wellhead
Bottom holeBarefoot interval
Annulus
Protective casing interval
Drill strings size
Diameter 01524m
Diameter 01524mDepth 4000ndash4960m
Inner diameter 022m
Outside diameter 01397mInner diameter 01214m
Outside diameter 00889mInner diameter 00702m
Outside diameter 00889mInner diameter 00381m
Depth 0ndash
Depth 0ndash1800m
Depth 1800ndash4930m
Depth 4930ndash4960m
4000m
Figure 5 The hole geometry and drilling assembly of the well
Table 1 Basic parameters for reservoir and drilling fluid used inreservoir characterization
Depth evaluation of the reservoir m 4156Reservoir thickness m 15Porosity 12Reservoir fluid volume factor m3stdm3 0008Reservoir fluid viscosity mPasdots 0035Reservoir compressibility Paminus1 116 times 10minus9
Reservoir fluid compressibility Paminus1 1177 times 10minus9
Geothermal temperature Ksdotmminus1 003Drilling fluid density at standard conditions gsdotcmminus3 104Drilling fluid viscosity at standard conditions mPasdots 20Injection gas specific gravity 1 097Injection gas viscosity at standard conditions mPasdots 0019
pressure and casing pressure for different time are plottedrespectively in Figures 6 and 7 It can be seen that thetransient fluctuations of standpipe pressure are more acutethan that of casing pressure In general this difference canbe aroused by unsteady drilling fluid and gas injection checkcalve measuring apparatus installed along drill string anddrill string vibrationThe casing pressure changing with timein Figure 7 indicates the different outlet gas rates or variedchoke opening Figure 8 shows the drilling fluid density asa function of time for outlet and injection respectivelyContrary to the standard drilling operations more accurateand automatic measurements of drilling fluid density can beobtained in real time utilizing instrumented standpipe andseparator drilling fluid outlet pipe using different pressure
2030 2118 2207 2254 234110
11
12
13
14
15
16
17
18
Stan
dpip
e pre
ssur
e (M
Pa)
Time1930
Figure 6 Data acquisitionmdashstandpipe pressure data versus time(2010-9-27)
1151 1342 1527 1715 1901 2052 2230250
275
300
325
350
375
400Ca
sing
pres
sure
(MPa
)
Time1000
Figure 7 Data acquisitionmdashcasing pressure data versus time (2010-9-27)
transducers not measured manually in intervals of 15 min-utes It is noted that the outlet drilling fluid density is slightlylower than that of injection fluid and fluctuates wildly Thistransient behavior of outlet drilling fluid density occurs as aresult of varied outlet gas rates and nonthorough degassing ofdrilling fluid In this study we monitor the total hydrocarboncontent of outlet gas and outlet gas rates to acquire thereservoir gas inflow rates in real timeThemeasured outlet gasrates and reservoir gas inflow rates are presented in Figure 9The real-time reservoir gas inflow rates absolutely criticalfor reservoir characterization are calculated using the outletgas rates and total hydrocarbon content in time of interestas shown in Figure 10 In sum the application of the newreal-time data monitoring system in this well helps drillingcontractor with good underbalanced drilling operations and
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
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Stochastic AnalysisInternational Journal of
4 Journal of Applied Mathematics
Choke manifold Combustion cell
Three-wayvalve
ThrottleMud pumps
BlenderThrottle
Portable gasanalyzer
Liquidflowmeter
Liquid flowmeterShale
shakers
Pressure transducer
Reserve pit
Mud pits
Pressuretransducer
Sampling
Booster
PC Reservoir characterization Compound logging data
Oil skimming tank
11
Sampling
Signal converser Incoherent receptor
Density measuring unit
Temperature transducer
Pressure transducer
Signal analyzer
Outlet (oil)
Pressure transducer
Gas flowmeter
Density measuring
unit
Throttle
Separator
Liquid flowmeter
Gas flowmeter
Injection (mud)
Drillstrings
Annulus
Injection(gas)
Injection(mixture)
Outlet
Outlet (mud)
Outlet (gas)
Outlet (mud)
Primary flow line
RBOP
Secondaryflow line
Nitrogengenerator
Compressor
Atmosphere
Solids disposal
Mud return line
Temperature transducer
deg100
50
minus0
minus10mV
Figure 1 A schematic of the placement of the real-time data monitoring system for aerated drilling
deg
Choke manifold Combustion cell
Three-wayvalve
ThrottleMud pumps Portable gas
analyzer
Liquidflowmeter
Liquid flowmeterShale
shakers
Pressure transducer
Reserve pit
Mud pits
Pressuretransducer
Sampling
100
50
PC Reservoir characterization Compound logging data
Oil skimming tank
11
Sampling
Signal converser Incoherent receptor
Density measuring unit
Pressure transducer
Signal analyzer
Outlet (oil)
Density measuring
unit
Throttle
Separator
Liquid flowmeter
Gas flowmeter
Injection (mud)
Injection (mud)
Mud return line Drillstrings
Annulus
Outlet
Outlet (mud)
Outlet (gas)
Outlet (mud)
Temperature transducer Primary flow line
RBOP
Secondaryflow line
Solids disposal
minus0
minus10mV
Figure 2 A schematic of the placement of the real-time data monitoring system for liquid-based underbalanced drilling
(i) The liquid phase fluids are incompressible and New-tonian
(ii) Properties of fluids are uniform and constant
(iii) The bubbles are spherical in shape having diameter asthe characteristic
(iv) The transverse lift force is neglected
(v) The turbulent dispersion force of gas phase is neglec-ted
(vi) The effects of breakup and coalescence of droplets andbubbles are neglected
(vii) Mass transfer effects are neglected
31 Model Development In this paper a transient model ofliquid-gas two-phase flow in wellbore is proposed on thebasis of the three-dimensional model averaged in time andspace given by Lahey andDrew [20]The governing equationsconsist of continuity equations for each component and a
Journal of Applied Mathematics 5
momentum conservation equation Such equations can bewritten as follows
gas continuity equation
120597 (120588
119892120572
119892)
120597119905
+
120597 (120588
119892120572
119892119906
119892)
120597119911
= 0
(1)
liquid continuity equation
120597 (120588
119897120572
119897)
120597119905
+
120597 (120588
119897120572
119897119906
119897)
120597119911
= 0(2)
gas momentum conservation equation
120597 (120588
119892120572
119892119906
119892)
120597119905
+
120597 (120588
119892120572
119892119906
2
119892
)
120597119911
+ 120572
119892
120597119901
120597119911
= minus120572
119892120588
119892119892 sin 120579 minus 119865
119889119892minus 119865V119898 minus 119865
119908119892
(3)
liquid momentum conservation equation
120597 (120588
119897120572
119897119906
119897)
120597119905
+
120597 (120588
119897120572
119897119906
2
119897
)
120597119911
+ 120572
119897
120597119901
120597119911
= minus120572
119897120588
119897119892 sin 120579 minus 119865
119889119892minus 119865V119898 minus 119865
119908119897
(4)
where 119901 is pressure 119892 is the acceleration due to gravity 120588is density 119906 is velocity 120572 is the volumetric fraction 120579 is thedeviation angle 119905 and 119911 are temporal and spatial coordi-nates 119865
119889is drag force 119865V119898 is virtual mass force 119865
119908is
wall shear force and the subscripts 119892 119897 represent gas andliquid respectively The indispensable closure relationshipsappearing in equations above are formulated and describedin Appendix A
Due to the mixture of gas-liquid two phases the dis-tribution relation of two-phase homogeneous fluid can benormalized as
120572
119892+ 120572
119897= 1 (5)
In this paper gas phase can be deemed as the ideal gas andcan be evaluated using the equation of state in the followingmanner
119901 = 119885120588
119892119877119879 (6)
where 119879 is temperature 119877 denotes the gas constant and 119885 isthe real gas deviation factor which is the function of pressuretemperature and the nature of the gas
In the transient liquid-gas two-phase flow model theheat transfer between wellbore and formation is consideredby introducing a wellbore heat transfer model during two-phase flow presented by Hasan and Kabir [21] based on arigorous energy balance equation for two-phase flow [22] Anexpression for fluid temperature in wellbore as a function ofwell depth and producing time is primarily given by
119879 = 119879
119890119894+ 120585 [1 minus 119890
119867120585
] (
119892
119892
119888
sin 120579
119869119862
119901
+ 120593 + 119892
119879sin 120579)
+ 119890
(119867minus119911)120585
(119879
119891119887ℎminus 119879
119890119887ℎ)
(7)
where 119879
119890119894is undisturbed formation temperature at given
depth 120585 is inverse relaxation distance 119867 is total welldepth from surface 119892
119888and 119869 represent conversion factors
119862
119901is the mean heat capacity of the multiphase fluid at
constant pressure 119892119879is geothermal temperature gradient
120593 is parameter combining the Joule-Thompson and kineticenergy effects 119879
119891119887ℎis fluid temperature at the bottom hole
and 119879
119890119887ℎis formation temperature at bottom hole Some
important parameters are discussed in detail in Appendix BIn the transient wellbore flow model we consider the
density behavior of drilling fluid under high pressure andhigh temperature conditions during underbalanced drillingoperation A more accurate analytical model for density-pressure-temperature dependence for drilling fluid in drillingproposed by Karstad and Aadnoy [23] was presented in thefollowing manner
120588
119897= 120588
119897119904119891119890
120574119901(119901minus119901119904119891)+120574119901119901(119901minus119901119904119891)2+120574119879(119879minus119879119904119891)+120574119879119879(119879minus119879119904119891)
2+120574119901119879(119901minus119901119904119891)(119879minus119879119904119891)
(8)
where 120588
119897119904119891is the drilling fluid density under standard con-
ditions 119879119904119891
is the standard temperature 120588119904119891
is the standardpressure and the values of 120574
119901 120574
119901119901 120574
119879 120574
119879119879 and 120574
119901119879are
essentially unknown and must be determined for differentmuds from density measurements at elevated pressures andtemperatures
Though we have made an assumption of gas liquid two-phase flow in wellbore the effect of cutting bed in horizontalwell on wellbore flow simulation has to be considered Thecutting bed existing in the horizontal annulus reduces theopen flow area of gas liquid two-phase fluid which is acritical factor in wellbore flow simulation In this paper weconsider the effect of cutting bed by evaluating the open flow
area of gas liquid two-phase fluid in horizontal annuluscausing the movement of cutting bed The cuttings trans-port in horizontal wellbore has been investigated by manyresearchers [24ndash30] In this paper we use a mechanics modelwith aerated drilling fluid proposed by Zhou [30] to predictthe movement of cutting bed and the cutting bed height
32 Numerical Solution In order to solve the model thefinite difference technique which is one of the most widelyused numerical methods is applied in this paper Thetechnique is implemented by replacing all derivatives bydifference quotients Owing to the introduction of analyticalexpression of temperature the model is easier to solve using
6 Journal of Applied Mathematics
the technique Discretization of governing equations can beobtained applying a first order downstream implicit schemefor time derivations For the stability of numerical solutionsthe donor cell concept is used The fluid exit conditions areassumed to be the same as the fluid conditions in the nodeitself The discretized form of governing equations can bewritten in the following matrix form
D119895(k0119895
) k119905+Δ119905119895
= E119895(k0119895
k119905119895
k119905+Δ119905119895minus1
) (9)
whereD is the coefficient matrix E is the independent vector119895 is cell number the superscripts 119905 and 119905+Δ119905 are the dependentvariables calculated at the old and new times respectively thesuperscript 0 represents the dummy variables for the iterativemethod and v is a column vector of dependent variablesgiven as follows
v = (119901 120572
119892 119906
119892 119906
119897)
119879
(10)
where the superscript 119879 indicates the transposeMechanistic models for two-phase flow in drill string and
annuli [31ndash33] are used to provide the necessary informationfor numerical calculation about flow patterns pressure dropsphase volumetric fractions and phase velocities in each oldtime node The wellbore fluid temperature at each grid pointcan be estimated using (7) In this paper we use the algorithmbased on the factorization of a matrix using a version of theGaussian elimination with partial pivoting
It is important to note that the numerical solution istransient due to the fact that almost all the transient termsare considered in our model In addition the numericalsolution of two-phase wellbore flow under constantly chang-ing flowing environmental can be given easily owing to theestablishment of real-time data monitoring system
4 Transient Well Influx Model
In underbalanced drilling the transient well influx can bedeemed as a complex well test The complexity arises fromthe fact that the boundary conditions vary with times invalue and type during the test because the well is con-tinuously increasing in length In the drilled part of thereservoir we have a Dirichlet boundary condition Insteadthe Neumann boundary condition is dealt with along thefuture well trajectory in the reservoir Also keep in mindthat the transient influx rates are influenced by variation inunderbalance and penetration rateTherefore the traditionalwell test techniques are not fit for the purpose of modelingtransient well influx during underbalanced drilling Becauseof the complexity of the problems a realistic model is neededto predict the transient well inflow while drilling
41 Mathematical Model Themodel in this paper representsa simplification of the actual reservoir It is assumed thatthe reservoir is symmetric around the well and possessesconstant reservoir and parameters During the transientperiod we assume that there is no pressure response from theborder of the reservoir For transient flow of a single phase
the governing differential equation can be given in the formof diffusivity equation
nabla
2
119901 =
120601120583119888
119896
120597119901
120597119905
(11)
where 120601 is porosity 119888 is reservoir compressibility 120583 is theviscosity of reservoir fluid and 119896 is the reservoir permeability
With the above assumption that there is no pressureresponse from the border of the reservoir the outer boundaryis given in the following Neumann manner
120597119901
120597119899
= 0(12)
where 119899 is the normal of the boundary surfacesEssentially the main difference of transient influx during
drilling with convention well test operations lies in the innerboundary which changes with time For the part of thereservoir penetrated by a horizontal well we have a Dirichletboundary condition
119901 = 119901
119908ℎ (13)
where 119901119908ℎ
is the pressure at bottom holeFor the undisturbed part of the reservoir the influx rates
are zero in other words the inner boundary conditionslikewise can be captured by the above Neumannmanner It isimportant to note that as a result of the continuous increasein well length the inner boundary conditions do not onlychange in value but in types as well Every drill step the partof the reservoir that is dominated by the Neumann conditiondecreases while the zone governed by theDirichlet conditionincreases This means that we have to deal with a new set ofequations with different boundary conditions for every stepdrill stepThus we are in dire need of new realistic expressionto describe the transient well influx during underbalanceddrilling
42 Approximate Analytical Solution To allow analyticalsolutions of the transient influx problem some essentialhypotheses are made in this paper We assume that thereservoir consists of a number of independent elements orzones as shown in Figure 3 It is assumed that the fluidflows along planes perpendicular to the well During under-balanced drilling a new zone is added to the well everystep in time The size of the time step and the thickness ofdrilled zones must conform to the penetration rate which isconsidered to be constant here It is assumed that productionfrom new added zone starts at the moment when it is beingpenetrated by drilling The total production rate at a giventime can be obtained by adding the production response ofindividual zones that time Thus the total production rate asa function of time can be given by
119902
119905119900119905(119905) = int
119911(119905)
0
119902
119908(119911 119905) 119889119911
(14)
Journal of Applied Mathematics 7
InjectionOutlet
Undisturbedreservoir
Opened reservoir elements
Permeability k1 k2 k3 k4
k1 k2 k3 k4
Figure 3 A schematic of a horizontal well drill into the reservoirconsists of a number of independent elements
where depth 119911 is a function of time 119905 and the penetrationrate 119906
119901 and 119902
119908(119909 119905) is the well influx from a unit thickness
Substitution of 119889119911 = 119906
119901119889119905 yields
119902
119905119900119905(119905) = int
119905
0
119902
119908(119911 120591) 119906
119901119889120591 (15)
Using Duhamelrsquos theorem van Kruijisdijk and Cox [6]proposed that the transient well influx for a given elementcan be rendered to a convolution of the underbalance andthe time derivative of the well influx for a constant andunit underbalance and rewrote the above equation in thefollowing manners
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (119901
119903119890119904minus 119901
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(16)
where 119902
119908119906(119905) denotes the unit-underbalanced inflow of unit
reservoir segment at the given time Θ represents the setof reservoir parameters that define the flow geometry andproperties 119901
119903119890119904is the reservoir pore pressure and 119901
119908is a
function of time and is defined as
119901
119908(119905) =
119901
119903119890119904for 119905 le 119905open (119911)
119901
119908ℎ(119905) for 119905 gt 119905open (119911)
(17)
The function 119905open(119911) represents the time atwhich the drillbit penetrates point 119911 thereby opening that point along thewell trajectory up to flow
To obtain an analytical solution of transient well inflowat any given time we need a realistic expression of the unit-underbalance transient inflow of each unit thickness segment119902
119908119906(119905) Based on the appropriate source functions in Laplace
space van Kruijisdijik [34] proposed the following analyticalsolution
119902
119908119906(119905) =
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(18)
where ℎ is the reservoir thickness 119903119908is the radius of the
wellbore119861119900is the volume factor of the reservoir fluid 119878
119911is the
effective skin due to vertical flow 1198861and 119886
2are the coefficient
and have respectively the values of 0611 and 1083 in the earlytime of transient influx
For gas reservoir the expression of the transient inflowis a bit different from (16) the analytical solution for oilreservoir proposed by van Kruijisdijk and Cox [6] Thecompressibility of gas decides the influx difference betweenoil and gas reservoirWe define the pseudopressure as follows
= 2int
119901
1199010
119901
120583
119892(119901)119885 (119901)
119889119901 (19)
where 119901
0is the known pressure for reference 120583
119892is the gas
viscosity and 119885 is the compressibility factor of the gas Thenthe total influx rates of gas reservoir during underbalanceddrilling can be given
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (
119903119890119904minus
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(20)
Analogously we rewrite the analytical expression of 119902119908119906
forgas reservoir in the following manner
119902
119908119906(119905) =
120587119896ℎ
119861
119892
119885
119904119888119879
119904119888120588
119892119904119888
119901
119904119888119879
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(21)
where the subscript denotes the standard state
5 Methodology of EstimatingReservoir Characterization
After establishing datamonitoring system in real time a tran-sient liquid-gas two-phase flow model in wellbore and wellinflux model during drilling have been derived Hereuntowe have reliable data acquisition approach and theoreticalmodel for reservoir characterization In this section let usfocus on specific approach to estimate reservoir properties Atfirst we will propose a new methodology to acquire reservoirpore pressure and then discuss how to extract the reservoirpermeability profiles during drilling
51 Reservoir Pore Pressure Inspired by the interestingmethodology of identifying reservoir pore pressure proposedby Kneissl [12] a new improved method of testing reservoirpore pressure is developed using different testing procedureavoiding the uncertainties affected by variations of fluid flowbehavior in the annulus sections and unpredictable inflowof new added zones It is noted that the idea of identifyingreservoir pore pressure by actively fluctuating the bottomhole pressure is still the key kernel thought of our methodFocusing on the new methodology a principal assumptionhas to be made that the reservoir drilled consists of differentzones with constant formation pressure coefficient whichcorresponds with the most common circumstances Withthe continuous pressure system assumption it is easy to
8 Journal of Applied Mathematics
obtain reservoir pore pressure of each zone by extracting thereservoir pressure coefficient when the reservoir is openedThis greatly simplifies the procedure of pore pressure testand avoids complex mathematical computation usually usedin other methods To eliminate the uncertainties of estimateresults introduced by continuous inflow of new zones it isneeded to stop drilling but keep circulation to begin thetesting operation when the first reservoir zone was openedwhich is the difference from Kneisslrsquos method in testingprocedure Taking into account the fact that only the first zonewas opened in the testing operation the transient inflow ofwell can be given by
119902
119908(119905) =
2120587119896ℎ (119901
119903119890119904minus 119901
119908(119905))
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(22)
It can be rewritten as
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(23)
At very short time the expression reduces to the followingmanner
lim119905rarr0
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
= lim119905rarr0
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911
(24)
which is entirely independent of the time and the downside of the equation can be considered constant for a givenreservoir It also can be interpreted that the transient inflowof well has a significant negative linear correlation with thepressure at bottom hole in the earliest hours of inflow Forthe inflow of well to become zero the reservoir pore pressureis approached by the pressure at bottom hole Thence wecan identify the reservoir pore pressure by searching forthe linear correlation between the inflow and pressure atbottom at the early stage of transient inflow This processis performed by introducing artificially fluctuations in thebottom hole pressure and by measuring the inflow rates andbottom hole pressure based on the real-time data monitoringsystem For aerated drilling the bottom hole pressure can beestimated using the transient wellbore flowmodel mentionedin this paper Figure 4 illustrates some details concerninghow to extract the reservoir pore pressure Here linear fittingof some measurement points is used to identify the linearcorrelation between thewell inflow and bottomhole pressureand the reservoir pore pressure can be read at the crossingof the best-fit regression line and the horizontal axis Forthe reliability of test results the number of testing pointsshould not be less than three Fluctuations of the bottom holepressure can be introduced by managing the choke valvechanging gas injection rates or pump rates To eliminatethe effects of variations of fluid flow in the wellbore onthe estimated results it is necessary to leave enough timeto capture relative steady inflow rates for each fluctuating
High
High
Low
0
qw
pw
Testing dataBest-fit regression line
Reservoir pressure
Figure 4 Reservoir pore pressure test by introducing fluctuation atthe bottom hole pressure
operation and the time needed lasts for a few minutes ormore than one hour which depends on well depth the typeof operations introducing the fluctuation in the bottom holepressure reservoir characteristics such as permeability andformation fluid properties and so on
Having acquired the reservoir pore pressure of the firstzone when the reservoir is opened the reservoir pressurecoefficient and pressure of subsequent zones can be obtainedduring drilling using a simple formula For the case wheremore than one reservoir with different pressure system wasdrilled new testing procedure should be repeated when newreservoir was opened The only difference is that the inflowmeasurements consist of the transient inflow response ofthe former reservoir and the transient well inflow of newreservoirrsquos first zone Here necessarymathematical treatmentof the inflow measurements is needed
52 Permeability Profiles To determine the reservoir perme-ability we make the simplifying assumption that the perme-ability is constant in specified zones of the well Transientinflux from each reservoir zone with different permeabilityat the time of interest constitutes the total production rates ofthewell which can be got from the real-time data acquisitionssystem The analytical expressions of total production ratesand unit-underbalance response of each zone which arerelated to the permeability have been established in the lastsection of this paper The reservoir pore pressure of eachreservoir zone can be calculated after testing the reservoirpressure coefficient just when the reservoir was opened Itis assumed that the porosity reservoir height and otherreservoir parameters apart from permeability are constantand known Theoretically the permeability of each reservoirzone can be easily determined using (18) and (21) Unfor-tunately the analytical expressions of the total productionrates are given in integral form which results in that theycannot readily be implemented in spreadsheet and calculator
Journal of Applied Mathematics 9
applications To facilitate the calculation a full discretizationof the total production rates formula is given instead of theintegral form in the following manner
119902
119905119900119905(119905) = 119906
119901(119901
119903119890119904minus 119901
119908)
119899=119905Δ119905
sum
119894=1
119902
119908119906119894(Θ
119894 119905 minus 119905
119894) Δ119905 (25)
where Δ119905 represents the time needed to penetrate througha reservoir element which is constant with the assumptionof the fixed penetration rate 119902
119908119906119894(Θ
119894 119905 minus 119905
119894) denotes unit-
underbalanced inflow of unit reservoir segment from zone 119894and 119905
119894denotes the time the wellbore reaches zone 119894 The value
of 119902119908119906119894
(Θ
119894 119905 minus 119905
119894) for nonpositive arguments is set equal to 0
The above discretization equation was given on the basisof a reasonable assumption that we have a constant underbal-ance which is realistic and is of engineering significance forunderbalanced drilling of a horizontal well
First we discuss how to extract the permeability of the1st reservoir zone The total production rates from the real-time monitoring system at the first time step when reservoiris opened can be simply considered to be the influx from thefirst zone Then we have the following formula
119902
119905119900119905(119905
1) = 119902
1199081(119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) 119902
1199081199061(Θ
1 119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
1ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896Δ119905120601120583119888119903
2
119908
(26)
Solving the equation above 1198961 the permeability of the 1st
reservoir zone can be given as follows
119896
1= (119898
2119902
1199081(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
1199081
(119905
1) Δ119905 +
119902
1199081(119905
1) 119878
119911
119898
1
)
2
(27)
where
119898
1=
2119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) ℎ119886
1
120583119861
119900119903
119908
119898
2=
119886
2
2119898
1119903
119908
radic120601120583119888
(28)
Analogously well influx from the reservoir element 119894 canbe given
119902
119908119894(119905
1)
= 119902
119905119900119905(119905
119894) minus
119894minus1
sum
119899=1
119902
119908119899(119905
119894minus119899)
= 119902
119905119900119905(119905
119894) minus 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
119894minus1
sum
119899=1
119902
119908119906119899(119905
119894minus 119905
119899)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
119894ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896
119894Δ119905120601120583119888119903
2
119908
(29)
where 119902tot(119905119894) represents the total production rates of the wellat time 119905
119894when the reservoir element is opened 119902
119908119906119899(119905
119894minus 119905
119899)
denotes the unit-underbalance transient influx response ofunit thickness reservoir from reservoir zone 119899 at time 119905
119894and
can be given using (21)Then we can extract the permeability of the reservoir
zone 119894 by
119896
119894= (119898
2119902
119908119894(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
119908119894
(119905
1) Δ119905 +
119902
119908119894(119905
1) 119878
119911
119898
1
)
2
(30)
Using the methodology the permeability of a set ofreservoir zones can be successively extracted as the reservoiris being penetrated by a horizontal well To facilitate theprecise calculation and estimate permeability profiles in timea computer procedure was used in this paper The success ofreservoir permeability estimation profits from reliable real-time data monitoring system advanced wellbore flow andreservoir model and an innovative reservoir pore pressuretest approach
6 Results and Discussion
The methodology presented in this paper has been used toidentify the reservoir pore pressure and permeability profilesof approximately 10 wells during underbalanced drilling inChina In order to illustrate the above approach in detail anactual horizontal well and gas reservoir are considered in thissection It is appropriate to emphasize that the well picked ascase study is the first successful application of this method-ology More exhaustive data and offset information from thiswell facilitate the effectiveness evaluation of this methodThereservoir dealt with here is the Ordovician carbonate gasreservoir with natural fractures as the dominant gas storagespaces and flowing channels To avoid lost circulation andformation damage the well is drilled underbalanced usingthe aerated clay-free drilling fluid while this is also beneficialfor well control Here nitrogen is used as the injection gasThe hole geometry and drilling assembly of this well wereillustrated in Figure 5 Some basic parameters for reservoirand drilling fluid used in reservoir characterization wereshown in Table 1
61 Data Acquisition in Real Time The real-time data mon-itoring system for aerated drilling presented in this paperwas used to acquire basic data for reservoir characterizationin real time The application of this system guaranteesthat the indispensable parameters are accurate and timelywhichmakes it possible to identify reservoir characterizationDuring drilling this system succeed in the integration of thedata from compound logging and our sensitive measuringinstruments and the digital microwave transmission wasproved to be realizable and reliable to deliver wirelesslydata Some typical acquired measurements plotted againsttime are shown in Figures 6ndash10 In order to illustrate thetransient behavior for different parameters the measuringtime for different parameters in figures differs The standpipe
10 Journal of Applied Mathematics
Drill bit
Cement
Casing
Drill strings
Wellhead
Bottom holeBarefoot interval
Annulus
Protective casing interval
Drill strings size
Diameter 01524m
Diameter 01524mDepth 4000ndash4960m
Inner diameter 022m
Outside diameter 01397mInner diameter 01214m
Outside diameter 00889mInner diameter 00702m
Outside diameter 00889mInner diameter 00381m
Depth 0ndash
Depth 0ndash1800m
Depth 1800ndash4930m
Depth 4930ndash4960m
4000m
Figure 5 The hole geometry and drilling assembly of the well
Table 1 Basic parameters for reservoir and drilling fluid used inreservoir characterization
Depth evaluation of the reservoir m 4156Reservoir thickness m 15Porosity 12Reservoir fluid volume factor m3stdm3 0008Reservoir fluid viscosity mPasdots 0035Reservoir compressibility Paminus1 116 times 10minus9
Reservoir fluid compressibility Paminus1 1177 times 10minus9
Geothermal temperature Ksdotmminus1 003Drilling fluid density at standard conditions gsdotcmminus3 104Drilling fluid viscosity at standard conditions mPasdots 20Injection gas specific gravity 1 097Injection gas viscosity at standard conditions mPasdots 0019
pressure and casing pressure for different time are plottedrespectively in Figures 6 and 7 It can be seen that thetransient fluctuations of standpipe pressure are more acutethan that of casing pressure In general this difference canbe aroused by unsteady drilling fluid and gas injection checkcalve measuring apparatus installed along drill string anddrill string vibrationThe casing pressure changing with timein Figure 7 indicates the different outlet gas rates or variedchoke opening Figure 8 shows the drilling fluid density asa function of time for outlet and injection respectivelyContrary to the standard drilling operations more accurateand automatic measurements of drilling fluid density can beobtained in real time utilizing instrumented standpipe andseparator drilling fluid outlet pipe using different pressure
2030 2118 2207 2254 234110
11
12
13
14
15
16
17
18
Stan
dpip
e pre
ssur
e (M
Pa)
Time1930
Figure 6 Data acquisitionmdashstandpipe pressure data versus time(2010-9-27)
1151 1342 1527 1715 1901 2052 2230250
275
300
325
350
375
400Ca
sing
pres
sure
(MPa
)
Time1000
Figure 7 Data acquisitionmdashcasing pressure data versus time (2010-9-27)
transducers not measured manually in intervals of 15 min-utes It is noted that the outlet drilling fluid density is slightlylower than that of injection fluid and fluctuates wildly Thistransient behavior of outlet drilling fluid density occurs as aresult of varied outlet gas rates and nonthorough degassing ofdrilling fluid In this study we monitor the total hydrocarboncontent of outlet gas and outlet gas rates to acquire thereservoir gas inflow rates in real timeThemeasured outlet gasrates and reservoir gas inflow rates are presented in Figure 9The real-time reservoir gas inflow rates absolutely criticalfor reservoir characterization are calculated using the outletgas rates and total hydrocarbon content in time of interestas shown in Figure 10 In sum the application of the newreal-time data monitoring system in this well helps drillingcontractor with good underbalanced drilling operations and
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
Journal of Applied Mathematics 5
momentum conservation equation Such equations can bewritten as follows
gas continuity equation
120597 (120588
119892120572
119892)
120597119905
+
120597 (120588
119892120572
119892119906
119892)
120597119911
= 0
(1)
liquid continuity equation
120597 (120588
119897120572
119897)
120597119905
+
120597 (120588
119897120572
119897119906
119897)
120597119911
= 0(2)
gas momentum conservation equation
120597 (120588
119892120572
119892119906
119892)
120597119905
+
120597 (120588
119892120572
119892119906
2
119892
)
120597119911
+ 120572
119892
120597119901
120597119911
= minus120572
119892120588
119892119892 sin 120579 minus 119865
119889119892minus 119865V119898 minus 119865
119908119892
(3)
liquid momentum conservation equation
120597 (120588
119897120572
119897119906
119897)
120597119905
+
120597 (120588
119897120572
119897119906
2
119897
)
120597119911
+ 120572
119897
120597119901
120597119911
= minus120572
119897120588
119897119892 sin 120579 minus 119865
119889119892minus 119865V119898 minus 119865
119908119897
(4)
where 119901 is pressure 119892 is the acceleration due to gravity 120588is density 119906 is velocity 120572 is the volumetric fraction 120579 is thedeviation angle 119905 and 119911 are temporal and spatial coordi-nates 119865
119889is drag force 119865V119898 is virtual mass force 119865
119908is
wall shear force and the subscripts 119892 119897 represent gas andliquid respectively The indispensable closure relationshipsappearing in equations above are formulated and describedin Appendix A
Due to the mixture of gas-liquid two phases the dis-tribution relation of two-phase homogeneous fluid can benormalized as
120572
119892+ 120572
119897= 1 (5)
In this paper gas phase can be deemed as the ideal gas andcan be evaluated using the equation of state in the followingmanner
119901 = 119885120588
119892119877119879 (6)
where 119879 is temperature 119877 denotes the gas constant and 119885 isthe real gas deviation factor which is the function of pressuretemperature and the nature of the gas
In the transient liquid-gas two-phase flow model theheat transfer between wellbore and formation is consideredby introducing a wellbore heat transfer model during two-phase flow presented by Hasan and Kabir [21] based on arigorous energy balance equation for two-phase flow [22] Anexpression for fluid temperature in wellbore as a function ofwell depth and producing time is primarily given by
119879 = 119879
119890119894+ 120585 [1 minus 119890
119867120585
] (
119892
119892
119888
sin 120579
119869119862
119901
+ 120593 + 119892
119879sin 120579)
+ 119890
(119867minus119911)120585
(119879
119891119887ℎminus 119879
119890119887ℎ)
(7)
where 119879
119890119894is undisturbed formation temperature at given
depth 120585 is inverse relaxation distance 119867 is total welldepth from surface 119892
119888and 119869 represent conversion factors
119862
119901is the mean heat capacity of the multiphase fluid at
constant pressure 119892119879is geothermal temperature gradient
120593 is parameter combining the Joule-Thompson and kineticenergy effects 119879
119891119887ℎis fluid temperature at the bottom hole
and 119879
119890119887ℎis formation temperature at bottom hole Some
important parameters are discussed in detail in Appendix BIn the transient wellbore flow model we consider the
density behavior of drilling fluid under high pressure andhigh temperature conditions during underbalanced drillingoperation A more accurate analytical model for density-pressure-temperature dependence for drilling fluid in drillingproposed by Karstad and Aadnoy [23] was presented in thefollowing manner
120588
119897= 120588
119897119904119891119890
120574119901(119901minus119901119904119891)+120574119901119901(119901minus119901119904119891)2+120574119879(119879minus119879119904119891)+120574119879119879(119879minus119879119904119891)
2+120574119901119879(119901minus119901119904119891)(119879minus119879119904119891)
(8)
where 120588
119897119904119891is the drilling fluid density under standard con-
ditions 119879119904119891
is the standard temperature 120588119904119891
is the standardpressure and the values of 120574
119901 120574
119901119901 120574
119879 120574
119879119879 and 120574
119901119879are
essentially unknown and must be determined for differentmuds from density measurements at elevated pressures andtemperatures
Though we have made an assumption of gas liquid two-phase flow in wellbore the effect of cutting bed in horizontalwell on wellbore flow simulation has to be considered Thecutting bed existing in the horizontal annulus reduces theopen flow area of gas liquid two-phase fluid which is acritical factor in wellbore flow simulation In this paper weconsider the effect of cutting bed by evaluating the open flow
area of gas liquid two-phase fluid in horizontal annuluscausing the movement of cutting bed The cuttings trans-port in horizontal wellbore has been investigated by manyresearchers [24ndash30] In this paper we use a mechanics modelwith aerated drilling fluid proposed by Zhou [30] to predictthe movement of cutting bed and the cutting bed height
32 Numerical Solution In order to solve the model thefinite difference technique which is one of the most widelyused numerical methods is applied in this paper Thetechnique is implemented by replacing all derivatives bydifference quotients Owing to the introduction of analyticalexpression of temperature the model is easier to solve using
6 Journal of Applied Mathematics
the technique Discretization of governing equations can beobtained applying a first order downstream implicit schemefor time derivations For the stability of numerical solutionsthe donor cell concept is used The fluid exit conditions areassumed to be the same as the fluid conditions in the nodeitself The discretized form of governing equations can bewritten in the following matrix form
D119895(k0119895
) k119905+Δ119905119895
= E119895(k0119895
k119905119895
k119905+Δ119905119895minus1
) (9)
whereD is the coefficient matrix E is the independent vector119895 is cell number the superscripts 119905 and 119905+Δ119905 are the dependentvariables calculated at the old and new times respectively thesuperscript 0 represents the dummy variables for the iterativemethod and v is a column vector of dependent variablesgiven as follows
v = (119901 120572
119892 119906
119892 119906
119897)
119879
(10)
where the superscript 119879 indicates the transposeMechanistic models for two-phase flow in drill string and
annuli [31ndash33] are used to provide the necessary informationfor numerical calculation about flow patterns pressure dropsphase volumetric fractions and phase velocities in each oldtime node The wellbore fluid temperature at each grid pointcan be estimated using (7) In this paper we use the algorithmbased on the factorization of a matrix using a version of theGaussian elimination with partial pivoting
It is important to note that the numerical solution istransient due to the fact that almost all the transient termsare considered in our model In addition the numericalsolution of two-phase wellbore flow under constantly chang-ing flowing environmental can be given easily owing to theestablishment of real-time data monitoring system
4 Transient Well Influx Model
In underbalanced drilling the transient well influx can bedeemed as a complex well test The complexity arises fromthe fact that the boundary conditions vary with times invalue and type during the test because the well is con-tinuously increasing in length In the drilled part of thereservoir we have a Dirichlet boundary condition Insteadthe Neumann boundary condition is dealt with along thefuture well trajectory in the reservoir Also keep in mindthat the transient influx rates are influenced by variation inunderbalance and penetration rateTherefore the traditionalwell test techniques are not fit for the purpose of modelingtransient well influx during underbalanced drilling Becauseof the complexity of the problems a realistic model is neededto predict the transient well inflow while drilling
41 Mathematical Model Themodel in this paper representsa simplification of the actual reservoir It is assumed thatthe reservoir is symmetric around the well and possessesconstant reservoir and parameters During the transientperiod we assume that there is no pressure response from theborder of the reservoir For transient flow of a single phase
the governing differential equation can be given in the formof diffusivity equation
nabla
2
119901 =
120601120583119888
119896
120597119901
120597119905
(11)
where 120601 is porosity 119888 is reservoir compressibility 120583 is theviscosity of reservoir fluid and 119896 is the reservoir permeability
With the above assumption that there is no pressureresponse from the border of the reservoir the outer boundaryis given in the following Neumann manner
120597119901
120597119899
= 0(12)
where 119899 is the normal of the boundary surfacesEssentially the main difference of transient influx during
drilling with convention well test operations lies in the innerboundary which changes with time For the part of thereservoir penetrated by a horizontal well we have a Dirichletboundary condition
119901 = 119901
119908ℎ (13)
where 119901119908ℎ
is the pressure at bottom holeFor the undisturbed part of the reservoir the influx rates
are zero in other words the inner boundary conditionslikewise can be captured by the above Neumannmanner It isimportant to note that as a result of the continuous increasein well length the inner boundary conditions do not onlychange in value but in types as well Every drill step the partof the reservoir that is dominated by the Neumann conditiondecreases while the zone governed by theDirichlet conditionincreases This means that we have to deal with a new set ofequations with different boundary conditions for every stepdrill stepThus we are in dire need of new realistic expressionto describe the transient well influx during underbalanceddrilling
42 Approximate Analytical Solution To allow analyticalsolutions of the transient influx problem some essentialhypotheses are made in this paper We assume that thereservoir consists of a number of independent elements orzones as shown in Figure 3 It is assumed that the fluidflows along planes perpendicular to the well During under-balanced drilling a new zone is added to the well everystep in time The size of the time step and the thickness ofdrilled zones must conform to the penetration rate which isconsidered to be constant here It is assumed that productionfrom new added zone starts at the moment when it is beingpenetrated by drilling The total production rate at a giventime can be obtained by adding the production response ofindividual zones that time Thus the total production rate asa function of time can be given by
119902
119905119900119905(119905) = int
119911(119905)
0
119902
119908(119911 119905) 119889119911
(14)
Journal of Applied Mathematics 7
InjectionOutlet
Undisturbedreservoir
Opened reservoir elements
Permeability k1 k2 k3 k4
k1 k2 k3 k4
Figure 3 A schematic of a horizontal well drill into the reservoirconsists of a number of independent elements
where depth 119911 is a function of time 119905 and the penetrationrate 119906
119901 and 119902
119908(119909 119905) is the well influx from a unit thickness
Substitution of 119889119911 = 119906
119901119889119905 yields
119902
119905119900119905(119905) = int
119905
0
119902
119908(119911 120591) 119906
119901119889120591 (15)
Using Duhamelrsquos theorem van Kruijisdijk and Cox [6]proposed that the transient well influx for a given elementcan be rendered to a convolution of the underbalance andthe time derivative of the well influx for a constant andunit underbalance and rewrote the above equation in thefollowing manners
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (119901
119903119890119904minus 119901
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(16)
where 119902
119908119906(119905) denotes the unit-underbalanced inflow of unit
reservoir segment at the given time Θ represents the setof reservoir parameters that define the flow geometry andproperties 119901
119903119890119904is the reservoir pore pressure and 119901
119908is a
function of time and is defined as
119901
119908(119905) =
119901
119903119890119904for 119905 le 119905open (119911)
119901
119908ℎ(119905) for 119905 gt 119905open (119911)
(17)
The function 119905open(119911) represents the time atwhich the drillbit penetrates point 119911 thereby opening that point along thewell trajectory up to flow
To obtain an analytical solution of transient well inflowat any given time we need a realistic expression of the unit-underbalance transient inflow of each unit thickness segment119902
119908119906(119905) Based on the appropriate source functions in Laplace
space van Kruijisdijik [34] proposed the following analyticalsolution
119902
119908119906(119905) =
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(18)
where ℎ is the reservoir thickness 119903119908is the radius of the
wellbore119861119900is the volume factor of the reservoir fluid 119878
119911is the
effective skin due to vertical flow 1198861and 119886
2are the coefficient
and have respectively the values of 0611 and 1083 in the earlytime of transient influx
For gas reservoir the expression of the transient inflowis a bit different from (16) the analytical solution for oilreservoir proposed by van Kruijisdijk and Cox [6] Thecompressibility of gas decides the influx difference betweenoil and gas reservoirWe define the pseudopressure as follows
= 2int
119901
1199010
119901
120583
119892(119901)119885 (119901)
119889119901 (19)
where 119901
0is the known pressure for reference 120583
119892is the gas
viscosity and 119885 is the compressibility factor of the gas Thenthe total influx rates of gas reservoir during underbalanceddrilling can be given
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (
119903119890119904minus
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(20)
Analogously we rewrite the analytical expression of 119902119908119906
forgas reservoir in the following manner
119902
119908119906(119905) =
120587119896ℎ
119861
119892
119885
119904119888119879
119904119888120588
119892119904119888
119901
119904119888119879
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(21)
where the subscript denotes the standard state
5 Methodology of EstimatingReservoir Characterization
After establishing datamonitoring system in real time a tran-sient liquid-gas two-phase flow model in wellbore and wellinflux model during drilling have been derived Hereuntowe have reliable data acquisition approach and theoreticalmodel for reservoir characterization In this section let usfocus on specific approach to estimate reservoir properties Atfirst we will propose a new methodology to acquire reservoirpore pressure and then discuss how to extract the reservoirpermeability profiles during drilling
51 Reservoir Pore Pressure Inspired by the interestingmethodology of identifying reservoir pore pressure proposedby Kneissl [12] a new improved method of testing reservoirpore pressure is developed using different testing procedureavoiding the uncertainties affected by variations of fluid flowbehavior in the annulus sections and unpredictable inflowof new added zones It is noted that the idea of identifyingreservoir pore pressure by actively fluctuating the bottomhole pressure is still the key kernel thought of our methodFocusing on the new methodology a principal assumptionhas to be made that the reservoir drilled consists of differentzones with constant formation pressure coefficient whichcorresponds with the most common circumstances Withthe continuous pressure system assumption it is easy to
8 Journal of Applied Mathematics
obtain reservoir pore pressure of each zone by extracting thereservoir pressure coefficient when the reservoir is openedThis greatly simplifies the procedure of pore pressure testand avoids complex mathematical computation usually usedin other methods To eliminate the uncertainties of estimateresults introduced by continuous inflow of new zones it isneeded to stop drilling but keep circulation to begin thetesting operation when the first reservoir zone was openedwhich is the difference from Kneisslrsquos method in testingprocedure Taking into account the fact that only the first zonewas opened in the testing operation the transient inflow ofwell can be given by
119902
119908(119905) =
2120587119896ℎ (119901
119903119890119904minus 119901
119908(119905))
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(22)
It can be rewritten as
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(23)
At very short time the expression reduces to the followingmanner
lim119905rarr0
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
= lim119905rarr0
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911
(24)
which is entirely independent of the time and the downside of the equation can be considered constant for a givenreservoir It also can be interpreted that the transient inflowof well has a significant negative linear correlation with thepressure at bottom hole in the earliest hours of inflow Forthe inflow of well to become zero the reservoir pore pressureis approached by the pressure at bottom hole Thence wecan identify the reservoir pore pressure by searching forthe linear correlation between the inflow and pressure atbottom at the early stage of transient inflow This processis performed by introducing artificially fluctuations in thebottom hole pressure and by measuring the inflow rates andbottom hole pressure based on the real-time data monitoringsystem For aerated drilling the bottom hole pressure can beestimated using the transient wellbore flowmodel mentionedin this paper Figure 4 illustrates some details concerninghow to extract the reservoir pore pressure Here linear fittingof some measurement points is used to identify the linearcorrelation between thewell inflow and bottomhole pressureand the reservoir pore pressure can be read at the crossingof the best-fit regression line and the horizontal axis Forthe reliability of test results the number of testing pointsshould not be less than three Fluctuations of the bottom holepressure can be introduced by managing the choke valvechanging gas injection rates or pump rates To eliminatethe effects of variations of fluid flow in the wellbore onthe estimated results it is necessary to leave enough timeto capture relative steady inflow rates for each fluctuating
High
High
Low
0
qw
pw
Testing dataBest-fit regression line
Reservoir pressure
Figure 4 Reservoir pore pressure test by introducing fluctuation atthe bottom hole pressure
operation and the time needed lasts for a few minutes ormore than one hour which depends on well depth the typeof operations introducing the fluctuation in the bottom holepressure reservoir characteristics such as permeability andformation fluid properties and so on
Having acquired the reservoir pore pressure of the firstzone when the reservoir is opened the reservoir pressurecoefficient and pressure of subsequent zones can be obtainedduring drilling using a simple formula For the case wheremore than one reservoir with different pressure system wasdrilled new testing procedure should be repeated when newreservoir was opened The only difference is that the inflowmeasurements consist of the transient inflow response ofthe former reservoir and the transient well inflow of newreservoirrsquos first zone Here necessarymathematical treatmentof the inflow measurements is needed
52 Permeability Profiles To determine the reservoir perme-ability we make the simplifying assumption that the perme-ability is constant in specified zones of the well Transientinflux from each reservoir zone with different permeabilityat the time of interest constitutes the total production rates ofthewell which can be got from the real-time data acquisitionssystem The analytical expressions of total production ratesand unit-underbalance response of each zone which arerelated to the permeability have been established in the lastsection of this paper The reservoir pore pressure of eachreservoir zone can be calculated after testing the reservoirpressure coefficient just when the reservoir was opened Itis assumed that the porosity reservoir height and otherreservoir parameters apart from permeability are constantand known Theoretically the permeability of each reservoirzone can be easily determined using (18) and (21) Unfor-tunately the analytical expressions of the total productionrates are given in integral form which results in that theycannot readily be implemented in spreadsheet and calculator
Journal of Applied Mathematics 9
applications To facilitate the calculation a full discretizationof the total production rates formula is given instead of theintegral form in the following manner
119902
119905119900119905(119905) = 119906
119901(119901
119903119890119904minus 119901
119908)
119899=119905Δ119905
sum
119894=1
119902
119908119906119894(Θ
119894 119905 minus 119905
119894) Δ119905 (25)
where Δ119905 represents the time needed to penetrate througha reservoir element which is constant with the assumptionof the fixed penetration rate 119902
119908119906119894(Θ
119894 119905 minus 119905
119894) denotes unit-
underbalanced inflow of unit reservoir segment from zone 119894and 119905
119894denotes the time the wellbore reaches zone 119894 The value
of 119902119908119906119894
(Θ
119894 119905 minus 119905
119894) for nonpositive arguments is set equal to 0
The above discretization equation was given on the basisof a reasonable assumption that we have a constant underbal-ance which is realistic and is of engineering significance forunderbalanced drilling of a horizontal well
First we discuss how to extract the permeability of the1st reservoir zone The total production rates from the real-time monitoring system at the first time step when reservoiris opened can be simply considered to be the influx from thefirst zone Then we have the following formula
119902
119905119900119905(119905
1) = 119902
1199081(119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) 119902
1199081199061(Θ
1 119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
1ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896Δ119905120601120583119888119903
2
119908
(26)
Solving the equation above 1198961 the permeability of the 1st
reservoir zone can be given as follows
119896
1= (119898
2119902
1199081(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
1199081
(119905
1) Δ119905 +
119902
1199081(119905
1) 119878
119911
119898
1
)
2
(27)
where
119898
1=
2119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) ℎ119886
1
120583119861
119900119903
119908
119898
2=
119886
2
2119898
1119903
119908
radic120601120583119888
(28)
Analogously well influx from the reservoir element 119894 canbe given
119902
119908119894(119905
1)
= 119902
119905119900119905(119905
119894) minus
119894minus1
sum
119899=1
119902
119908119899(119905
119894minus119899)
= 119902
119905119900119905(119905
119894) minus 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
119894minus1
sum
119899=1
119902
119908119906119899(119905
119894minus 119905
119899)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
119894ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896
119894Δ119905120601120583119888119903
2
119908
(29)
where 119902tot(119905119894) represents the total production rates of the wellat time 119905
119894when the reservoir element is opened 119902
119908119906119899(119905
119894minus 119905
119899)
denotes the unit-underbalance transient influx response ofunit thickness reservoir from reservoir zone 119899 at time 119905
119894and
can be given using (21)Then we can extract the permeability of the reservoir
zone 119894 by
119896
119894= (119898
2119902
119908119894(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
119908119894
(119905
1) Δ119905 +
119902
119908119894(119905
1) 119878
119911
119898
1
)
2
(30)
Using the methodology the permeability of a set ofreservoir zones can be successively extracted as the reservoiris being penetrated by a horizontal well To facilitate theprecise calculation and estimate permeability profiles in timea computer procedure was used in this paper The success ofreservoir permeability estimation profits from reliable real-time data monitoring system advanced wellbore flow andreservoir model and an innovative reservoir pore pressuretest approach
6 Results and Discussion
The methodology presented in this paper has been used toidentify the reservoir pore pressure and permeability profilesof approximately 10 wells during underbalanced drilling inChina In order to illustrate the above approach in detail anactual horizontal well and gas reservoir are considered in thissection It is appropriate to emphasize that the well picked ascase study is the first successful application of this method-ology More exhaustive data and offset information from thiswell facilitate the effectiveness evaluation of this methodThereservoir dealt with here is the Ordovician carbonate gasreservoir with natural fractures as the dominant gas storagespaces and flowing channels To avoid lost circulation andformation damage the well is drilled underbalanced usingthe aerated clay-free drilling fluid while this is also beneficialfor well control Here nitrogen is used as the injection gasThe hole geometry and drilling assembly of this well wereillustrated in Figure 5 Some basic parameters for reservoirand drilling fluid used in reservoir characterization wereshown in Table 1
61 Data Acquisition in Real Time The real-time data mon-itoring system for aerated drilling presented in this paperwas used to acquire basic data for reservoir characterizationin real time The application of this system guaranteesthat the indispensable parameters are accurate and timelywhichmakes it possible to identify reservoir characterizationDuring drilling this system succeed in the integration of thedata from compound logging and our sensitive measuringinstruments and the digital microwave transmission wasproved to be realizable and reliable to deliver wirelesslydata Some typical acquired measurements plotted againsttime are shown in Figures 6ndash10 In order to illustrate thetransient behavior for different parameters the measuringtime for different parameters in figures differs The standpipe
10 Journal of Applied Mathematics
Drill bit
Cement
Casing
Drill strings
Wellhead
Bottom holeBarefoot interval
Annulus
Protective casing interval
Drill strings size
Diameter 01524m
Diameter 01524mDepth 4000ndash4960m
Inner diameter 022m
Outside diameter 01397mInner diameter 01214m
Outside diameter 00889mInner diameter 00702m
Outside diameter 00889mInner diameter 00381m
Depth 0ndash
Depth 0ndash1800m
Depth 1800ndash4930m
Depth 4930ndash4960m
4000m
Figure 5 The hole geometry and drilling assembly of the well
Table 1 Basic parameters for reservoir and drilling fluid used inreservoir characterization
Depth evaluation of the reservoir m 4156Reservoir thickness m 15Porosity 12Reservoir fluid volume factor m3stdm3 0008Reservoir fluid viscosity mPasdots 0035Reservoir compressibility Paminus1 116 times 10minus9
Reservoir fluid compressibility Paminus1 1177 times 10minus9
Geothermal temperature Ksdotmminus1 003Drilling fluid density at standard conditions gsdotcmminus3 104Drilling fluid viscosity at standard conditions mPasdots 20Injection gas specific gravity 1 097Injection gas viscosity at standard conditions mPasdots 0019
pressure and casing pressure for different time are plottedrespectively in Figures 6 and 7 It can be seen that thetransient fluctuations of standpipe pressure are more acutethan that of casing pressure In general this difference canbe aroused by unsteady drilling fluid and gas injection checkcalve measuring apparatus installed along drill string anddrill string vibrationThe casing pressure changing with timein Figure 7 indicates the different outlet gas rates or variedchoke opening Figure 8 shows the drilling fluid density asa function of time for outlet and injection respectivelyContrary to the standard drilling operations more accurateand automatic measurements of drilling fluid density can beobtained in real time utilizing instrumented standpipe andseparator drilling fluid outlet pipe using different pressure
2030 2118 2207 2254 234110
11
12
13
14
15
16
17
18
Stan
dpip
e pre
ssur
e (M
Pa)
Time1930
Figure 6 Data acquisitionmdashstandpipe pressure data versus time(2010-9-27)
1151 1342 1527 1715 1901 2052 2230250
275
300
325
350
375
400Ca
sing
pres
sure
(MPa
)
Time1000
Figure 7 Data acquisitionmdashcasing pressure data versus time (2010-9-27)
transducers not measured manually in intervals of 15 min-utes It is noted that the outlet drilling fluid density is slightlylower than that of injection fluid and fluctuates wildly Thistransient behavior of outlet drilling fluid density occurs as aresult of varied outlet gas rates and nonthorough degassing ofdrilling fluid In this study we monitor the total hydrocarboncontent of outlet gas and outlet gas rates to acquire thereservoir gas inflow rates in real timeThemeasured outlet gasrates and reservoir gas inflow rates are presented in Figure 9The real-time reservoir gas inflow rates absolutely criticalfor reservoir characterization are calculated using the outletgas rates and total hydrocarbon content in time of interestas shown in Figure 10 In sum the application of the newreal-time data monitoring system in this well helps drillingcontractor with good underbalanced drilling operations and
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
6 Journal of Applied Mathematics
the technique Discretization of governing equations can beobtained applying a first order downstream implicit schemefor time derivations For the stability of numerical solutionsthe donor cell concept is used The fluid exit conditions areassumed to be the same as the fluid conditions in the nodeitself The discretized form of governing equations can bewritten in the following matrix form
D119895(k0119895
) k119905+Δ119905119895
= E119895(k0119895
k119905119895
k119905+Δ119905119895minus1
) (9)
whereD is the coefficient matrix E is the independent vector119895 is cell number the superscripts 119905 and 119905+Δ119905 are the dependentvariables calculated at the old and new times respectively thesuperscript 0 represents the dummy variables for the iterativemethod and v is a column vector of dependent variablesgiven as follows
v = (119901 120572
119892 119906
119892 119906
119897)
119879
(10)
where the superscript 119879 indicates the transposeMechanistic models for two-phase flow in drill string and
annuli [31ndash33] are used to provide the necessary informationfor numerical calculation about flow patterns pressure dropsphase volumetric fractions and phase velocities in each oldtime node The wellbore fluid temperature at each grid pointcan be estimated using (7) In this paper we use the algorithmbased on the factorization of a matrix using a version of theGaussian elimination with partial pivoting
It is important to note that the numerical solution istransient due to the fact that almost all the transient termsare considered in our model In addition the numericalsolution of two-phase wellbore flow under constantly chang-ing flowing environmental can be given easily owing to theestablishment of real-time data monitoring system
4 Transient Well Influx Model
In underbalanced drilling the transient well influx can bedeemed as a complex well test The complexity arises fromthe fact that the boundary conditions vary with times invalue and type during the test because the well is con-tinuously increasing in length In the drilled part of thereservoir we have a Dirichlet boundary condition Insteadthe Neumann boundary condition is dealt with along thefuture well trajectory in the reservoir Also keep in mindthat the transient influx rates are influenced by variation inunderbalance and penetration rateTherefore the traditionalwell test techniques are not fit for the purpose of modelingtransient well influx during underbalanced drilling Becauseof the complexity of the problems a realistic model is neededto predict the transient well inflow while drilling
41 Mathematical Model Themodel in this paper representsa simplification of the actual reservoir It is assumed thatthe reservoir is symmetric around the well and possessesconstant reservoir and parameters During the transientperiod we assume that there is no pressure response from theborder of the reservoir For transient flow of a single phase
the governing differential equation can be given in the formof diffusivity equation
nabla
2
119901 =
120601120583119888
119896
120597119901
120597119905
(11)
where 120601 is porosity 119888 is reservoir compressibility 120583 is theviscosity of reservoir fluid and 119896 is the reservoir permeability
With the above assumption that there is no pressureresponse from the border of the reservoir the outer boundaryis given in the following Neumann manner
120597119901
120597119899
= 0(12)
where 119899 is the normal of the boundary surfacesEssentially the main difference of transient influx during
drilling with convention well test operations lies in the innerboundary which changes with time For the part of thereservoir penetrated by a horizontal well we have a Dirichletboundary condition
119901 = 119901
119908ℎ (13)
where 119901119908ℎ
is the pressure at bottom holeFor the undisturbed part of the reservoir the influx rates
are zero in other words the inner boundary conditionslikewise can be captured by the above Neumannmanner It isimportant to note that as a result of the continuous increasein well length the inner boundary conditions do not onlychange in value but in types as well Every drill step the partof the reservoir that is dominated by the Neumann conditiondecreases while the zone governed by theDirichlet conditionincreases This means that we have to deal with a new set ofequations with different boundary conditions for every stepdrill stepThus we are in dire need of new realistic expressionto describe the transient well influx during underbalanceddrilling
42 Approximate Analytical Solution To allow analyticalsolutions of the transient influx problem some essentialhypotheses are made in this paper We assume that thereservoir consists of a number of independent elements orzones as shown in Figure 3 It is assumed that the fluidflows along planes perpendicular to the well During under-balanced drilling a new zone is added to the well everystep in time The size of the time step and the thickness ofdrilled zones must conform to the penetration rate which isconsidered to be constant here It is assumed that productionfrom new added zone starts at the moment when it is beingpenetrated by drilling The total production rate at a giventime can be obtained by adding the production response ofindividual zones that time Thus the total production rate asa function of time can be given by
119902
119905119900119905(119905) = int
119911(119905)
0
119902
119908(119911 119905) 119889119911
(14)
Journal of Applied Mathematics 7
InjectionOutlet
Undisturbedreservoir
Opened reservoir elements
Permeability k1 k2 k3 k4
k1 k2 k3 k4
Figure 3 A schematic of a horizontal well drill into the reservoirconsists of a number of independent elements
where depth 119911 is a function of time 119905 and the penetrationrate 119906
119901 and 119902
119908(119909 119905) is the well influx from a unit thickness
Substitution of 119889119911 = 119906
119901119889119905 yields
119902
119905119900119905(119905) = int
119905
0
119902
119908(119911 120591) 119906
119901119889120591 (15)
Using Duhamelrsquos theorem van Kruijisdijk and Cox [6]proposed that the transient well influx for a given elementcan be rendered to a convolution of the underbalance andthe time derivative of the well influx for a constant andunit underbalance and rewrote the above equation in thefollowing manners
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (119901
119903119890119904minus 119901
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(16)
where 119902
119908119906(119905) denotes the unit-underbalanced inflow of unit
reservoir segment at the given time Θ represents the setof reservoir parameters that define the flow geometry andproperties 119901
119903119890119904is the reservoir pore pressure and 119901
119908is a
function of time and is defined as
119901
119908(119905) =
119901
119903119890119904for 119905 le 119905open (119911)
119901
119908ℎ(119905) for 119905 gt 119905open (119911)
(17)
The function 119905open(119911) represents the time atwhich the drillbit penetrates point 119911 thereby opening that point along thewell trajectory up to flow
To obtain an analytical solution of transient well inflowat any given time we need a realistic expression of the unit-underbalance transient inflow of each unit thickness segment119902
119908119906(119905) Based on the appropriate source functions in Laplace
space van Kruijisdijik [34] proposed the following analyticalsolution
119902
119908119906(119905) =
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(18)
where ℎ is the reservoir thickness 119903119908is the radius of the
wellbore119861119900is the volume factor of the reservoir fluid 119878
119911is the
effective skin due to vertical flow 1198861and 119886
2are the coefficient
and have respectively the values of 0611 and 1083 in the earlytime of transient influx
For gas reservoir the expression of the transient inflowis a bit different from (16) the analytical solution for oilreservoir proposed by van Kruijisdijk and Cox [6] Thecompressibility of gas decides the influx difference betweenoil and gas reservoirWe define the pseudopressure as follows
= 2int
119901
1199010
119901
120583
119892(119901)119885 (119901)
119889119901 (19)
where 119901
0is the known pressure for reference 120583
119892is the gas
viscosity and 119885 is the compressibility factor of the gas Thenthe total influx rates of gas reservoir during underbalanceddrilling can be given
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (
119903119890119904minus
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(20)
Analogously we rewrite the analytical expression of 119902119908119906
forgas reservoir in the following manner
119902
119908119906(119905) =
120587119896ℎ
119861
119892
119885
119904119888119879
119904119888120588
119892119904119888
119901
119904119888119879
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(21)
where the subscript denotes the standard state
5 Methodology of EstimatingReservoir Characterization
After establishing datamonitoring system in real time a tran-sient liquid-gas two-phase flow model in wellbore and wellinflux model during drilling have been derived Hereuntowe have reliable data acquisition approach and theoreticalmodel for reservoir characterization In this section let usfocus on specific approach to estimate reservoir properties Atfirst we will propose a new methodology to acquire reservoirpore pressure and then discuss how to extract the reservoirpermeability profiles during drilling
51 Reservoir Pore Pressure Inspired by the interestingmethodology of identifying reservoir pore pressure proposedby Kneissl [12] a new improved method of testing reservoirpore pressure is developed using different testing procedureavoiding the uncertainties affected by variations of fluid flowbehavior in the annulus sections and unpredictable inflowof new added zones It is noted that the idea of identifyingreservoir pore pressure by actively fluctuating the bottomhole pressure is still the key kernel thought of our methodFocusing on the new methodology a principal assumptionhas to be made that the reservoir drilled consists of differentzones with constant formation pressure coefficient whichcorresponds with the most common circumstances Withthe continuous pressure system assumption it is easy to
8 Journal of Applied Mathematics
obtain reservoir pore pressure of each zone by extracting thereservoir pressure coefficient when the reservoir is openedThis greatly simplifies the procedure of pore pressure testand avoids complex mathematical computation usually usedin other methods To eliminate the uncertainties of estimateresults introduced by continuous inflow of new zones it isneeded to stop drilling but keep circulation to begin thetesting operation when the first reservoir zone was openedwhich is the difference from Kneisslrsquos method in testingprocedure Taking into account the fact that only the first zonewas opened in the testing operation the transient inflow ofwell can be given by
119902
119908(119905) =
2120587119896ℎ (119901
119903119890119904minus 119901
119908(119905))
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(22)
It can be rewritten as
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(23)
At very short time the expression reduces to the followingmanner
lim119905rarr0
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
= lim119905rarr0
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911
(24)
which is entirely independent of the time and the downside of the equation can be considered constant for a givenreservoir It also can be interpreted that the transient inflowof well has a significant negative linear correlation with thepressure at bottom hole in the earliest hours of inflow Forthe inflow of well to become zero the reservoir pore pressureis approached by the pressure at bottom hole Thence wecan identify the reservoir pore pressure by searching forthe linear correlation between the inflow and pressure atbottom at the early stage of transient inflow This processis performed by introducing artificially fluctuations in thebottom hole pressure and by measuring the inflow rates andbottom hole pressure based on the real-time data monitoringsystem For aerated drilling the bottom hole pressure can beestimated using the transient wellbore flowmodel mentionedin this paper Figure 4 illustrates some details concerninghow to extract the reservoir pore pressure Here linear fittingof some measurement points is used to identify the linearcorrelation between thewell inflow and bottomhole pressureand the reservoir pore pressure can be read at the crossingof the best-fit regression line and the horizontal axis Forthe reliability of test results the number of testing pointsshould not be less than three Fluctuations of the bottom holepressure can be introduced by managing the choke valvechanging gas injection rates or pump rates To eliminatethe effects of variations of fluid flow in the wellbore onthe estimated results it is necessary to leave enough timeto capture relative steady inflow rates for each fluctuating
High
High
Low
0
qw
pw
Testing dataBest-fit regression line
Reservoir pressure
Figure 4 Reservoir pore pressure test by introducing fluctuation atthe bottom hole pressure
operation and the time needed lasts for a few minutes ormore than one hour which depends on well depth the typeof operations introducing the fluctuation in the bottom holepressure reservoir characteristics such as permeability andformation fluid properties and so on
Having acquired the reservoir pore pressure of the firstzone when the reservoir is opened the reservoir pressurecoefficient and pressure of subsequent zones can be obtainedduring drilling using a simple formula For the case wheremore than one reservoir with different pressure system wasdrilled new testing procedure should be repeated when newreservoir was opened The only difference is that the inflowmeasurements consist of the transient inflow response ofthe former reservoir and the transient well inflow of newreservoirrsquos first zone Here necessarymathematical treatmentof the inflow measurements is needed
52 Permeability Profiles To determine the reservoir perme-ability we make the simplifying assumption that the perme-ability is constant in specified zones of the well Transientinflux from each reservoir zone with different permeabilityat the time of interest constitutes the total production rates ofthewell which can be got from the real-time data acquisitionssystem The analytical expressions of total production ratesand unit-underbalance response of each zone which arerelated to the permeability have been established in the lastsection of this paper The reservoir pore pressure of eachreservoir zone can be calculated after testing the reservoirpressure coefficient just when the reservoir was opened Itis assumed that the porosity reservoir height and otherreservoir parameters apart from permeability are constantand known Theoretically the permeability of each reservoirzone can be easily determined using (18) and (21) Unfor-tunately the analytical expressions of the total productionrates are given in integral form which results in that theycannot readily be implemented in spreadsheet and calculator
Journal of Applied Mathematics 9
applications To facilitate the calculation a full discretizationof the total production rates formula is given instead of theintegral form in the following manner
119902
119905119900119905(119905) = 119906
119901(119901
119903119890119904minus 119901
119908)
119899=119905Δ119905
sum
119894=1
119902
119908119906119894(Θ
119894 119905 minus 119905
119894) Δ119905 (25)
where Δ119905 represents the time needed to penetrate througha reservoir element which is constant with the assumptionof the fixed penetration rate 119902
119908119906119894(Θ
119894 119905 minus 119905
119894) denotes unit-
underbalanced inflow of unit reservoir segment from zone 119894and 119905
119894denotes the time the wellbore reaches zone 119894 The value
of 119902119908119906119894
(Θ
119894 119905 minus 119905
119894) for nonpositive arguments is set equal to 0
The above discretization equation was given on the basisof a reasonable assumption that we have a constant underbal-ance which is realistic and is of engineering significance forunderbalanced drilling of a horizontal well
First we discuss how to extract the permeability of the1st reservoir zone The total production rates from the real-time monitoring system at the first time step when reservoiris opened can be simply considered to be the influx from thefirst zone Then we have the following formula
119902
119905119900119905(119905
1) = 119902
1199081(119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) 119902
1199081199061(Θ
1 119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
1ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896Δ119905120601120583119888119903
2
119908
(26)
Solving the equation above 1198961 the permeability of the 1st
reservoir zone can be given as follows
119896
1= (119898
2119902
1199081(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
1199081
(119905
1) Δ119905 +
119902
1199081(119905
1) 119878
119911
119898
1
)
2
(27)
where
119898
1=
2119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) ℎ119886
1
120583119861
119900119903
119908
119898
2=
119886
2
2119898
1119903
119908
radic120601120583119888
(28)
Analogously well influx from the reservoir element 119894 canbe given
119902
119908119894(119905
1)
= 119902
119905119900119905(119905
119894) minus
119894minus1
sum
119899=1
119902
119908119899(119905
119894minus119899)
= 119902
119905119900119905(119905
119894) minus 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
119894minus1
sum
119899=1
119902
119908119906119899(119905
119894minus 119905
119899)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
119894ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896
119894Δ119905120601120583119888119903
2
119908
(29)
where 119902tot(119905119894) represents the total production rates of the wellat time 119905
119894when the reservoir element is opened 119902
119908119906119899(119905
119894minus 119905
119899)
denotes the unit-underbalance transient influx response ofunit thickness reservoir from reservoir zone 119899 at time 119905
119894and
can be given using (21)Then we can extract the permeability of the reservoir
zone 119894 by
119896
119894= (119898
2119902
119908119894(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
119908119894
(119905
1) Δ119905 +
119902
119908119894(119905
1) 119878
119911
119898
1
)
2
(30)
Using the methodology the permeability of a set ofreservoir zones can be successively extracted as the reservoiris being penetrated by a horizontal well To facilitate theprecise calculation and estimate permeability profiles in timea computer procedure was used in this paper The success ofreservoir permeability estimation profits from reliable real-time data monitoring system advanced wellbore flow andreservoir model and an innovative reservoir pore pressuretest approach
6 Results and Discussion
The methodology presented in this paper has been used toidentify the reservoir pore pressure and permeability profilesof approximately 10 wells during underbalanced drilling inChina In order to illustrate the above approach in detail anactual horizontal well and gas reservoir are considered in thissection It is appropriate to emphasize that the well picked ascase study is the first successful application of this method-ology More exhaustive data and offset information from thiswell facilitate the effectiveness evaluation of this methodThereservoir dealt with here is the Ordovician carbonate gasreservoir with natural fractures as the dominant gas storagespaces and flowing channels To avoid lost circulation andformation damage the well is drilled underbalanced usingthe aerated clay-free drilling fluid while this is also beneficialfor well control Here nitrogen is used as the injection gasThe hole geometry and drilling assembly of this well wereillustrated in Figure 5 Some basic parameters for reservoirand drilling fluid used in reservoir characterization wereshown in Table 1
61 Data Acquisition in Real Time The real-time data mon-itoring system for aerated drilling presented in this paperwas used to acquire basic data for reservoir characterizationin real time The application of this system guaranteesthat the indispensable parameters are accurate and timelywhichmakes it possible to identify reservoir characterizationDuring drilling this system succeed in the integration of thedata from compound logging and our sensitive measuringinstruments and the digital microwave transmission wasproved to be realizable and reliable to deliver wirelesslydata Some typical acquired measurements plotted againsttime are shown in Figures 6ndash10 In order to illustrate thetransient behavior for different parameters the measuringtime for different parameters in figures differs The standpipe
10 Journal of Applied Mathematics
Drill bit
Cement
Casing
Drill strings
Wellhead
Bottom holeBarefoot interval
Annulus
Protective casing interval
Drill strings size
Diameter 01524m
Diameter 01524mDepth 4000ndash4960m
Inner diameter 022m
Outside diameter 01397mInner diameter 01214m
Outside diameter 00889mInner diameter 00702m
Outside diameter 00889mInner diameter 00381m
Depth 0ndash
Depth 0ndash1800m
Depth 1800ndash4930m
Depth 4930ndash4960m
4000m
Figure 5 The hole geometry and drilling assembly of the well
Table 1 Basic parameters for reservoir and drilling fluid used inreservoir characterization
Depth evaluation of the reservoir m 4156Reservoir thickness m 15Porosity 12Reservoir fluid volume factor m3stdm3 0008Reservoir fluid viscosity mPasdots 0035Reservoir compressibility Paminus1 116 times 10minus9
Reservoir fluid compressibility Paminus1 1177 times 10minus9
Geothermal temperature Ksdotmminus1 003Drilling fluid density at standard conditions gsdotcmminus3 104Drilling fluid viscosity at standard conditions mPasdots 20Injection gas specific gravity 1 097Injection gas viscosity at standard conditions mPasdots 0019
pressure and casing pressure for different time are plottedrespectively in Figures 6 and 7 It can be seen that thetransient fluctuations of standpipe pressure are more acutethan that of casing pressure In general this difference canbe aroused by unsteady drilling fluid and gas injection checkcalve measuring apparatus installed along drill string anddrill string vibrationThe casing pressure changing with timein Figure 7 indicates the different outlet gas rates or variedchoke opening Figure 8 shows the drilling fluid density asa function of time for outlet and injection respectivelyContrary to the standard drilling operations more accurateand automatic measurements of drilling fluid density can beobtained in real time utilizing instrumented standpipe andseparator drilling fluid outlet pipe using different pressure
2030 2118 2207 2254 234110
11
12
13
14
15
16
17
18
Stan
dpip
e pre
ssur
e (M
Pa)
Time1930
Figure 6 Data acquisitionmdashstandpipe pressure data versus time(2010-9-27)
1151 1342 1527 1715 1901 2052 2230250
275
300
325
350
375
400Ca
sing
pres
sure
(MPa
)
Time1000
Figure 7 Data acquisitionmdashcasing pressure data versus time (2010-9-27)
transducers not measured manually in intervals of 15 min-utes It is noted that the outlet drilling fluid density is slightlylower than that of injection fluid and fluctuates wildly Thistransient behavior of outlet drilling fluid density occurs as aresult of varied outlet gas rates and nonthorough degassing ofdrilling fluid In this study we monitor the total hydrocarboncontent of outlet gas and outlet gas rates to acquire thereservoir gas inflow rates in real timeThemeasured outlet gasrates and reservoir gas inflow rates are presented in Figure 9The real-time reservoir gas inflow rates absolutely criticalfor reservoir characterization are calculated using the outletgas rates and total hydrocarbon content in time of interestas shown in Figure 10 In sum the application of the newreal-time data monitoring system in this well helps drillingcontractor with good underbalanced drilling operations and
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
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Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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Differential EquationsInternational Journal of
Volume 2014
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Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
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Algebra
Discrete Dynamics in Nature and Society
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Decision SciencesAdvances in
Discrete MathematicsJournal of
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Stochastic AnalysisInternational Journal of
Journal of Applied Mathematics 7
InjectionOutlet
Undisturbedreservoir
Opened reservoir elements
Permeability k1 k2 k3 k4
k1 k2 k3 k4
Figure 3 A schematic of a horizontal well drill into the reservoirconsists of a number of independent elements
where depth 119911 is a function of time 119905 and the penetrationrate 119906
119901 and 119902
119908(119909 119905) is the well influx from a unit thickness
Substitution of 119889119911 = 119906
119901119889119905 yields
119902
119905119900119905(119905) = int
119905
0
119902
119908(119911 120591) 119906
119901119889120591 (15)
Using Duhamelrsquos theorem van Kruijisdijk and Cox [6]proposed that the transient well influx for a given elementcan be rendered to a convolution of the underbalance andthe time derivative of the well influx for a constant andunit underbalance and rewrote the above equation in thefollowing manners
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (119901
119903119890119904minus 119901
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(16)
where 119902
119908119906(119905) denotes the unit-underbalanced inflow of unit
reservoir segment at the given time Θ represents the setof reservoir parameters that define the flow geometry andproperties 119901
119903119890119904is the reservoir pore pressure and 119901
119908is a
function of time and is defined as
119901
119908(119905) =
119901
119903119890119904for 119905 le 119905open (119911)
119901
119908ℎ(119905) for 119905 gt 119905open (119911)
(17)
The function 119905open(119911) represents the time atwhich the drillbit penetrates point 119911 thereby opening that point along thewell trajectory up to flow
To obtain an analytical solution of transient well inflowat any given time we need a realistic expression of the unit-underbalance transient inflow of each unit thickness segment119902
119908119906(119905) Based on the appropriate source functions in Laplace
space van Kruijisdijik [34] proposed the following analyticalsolution
119902
119908119906(119905) =
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(18)
where ℎ is the reservoir thickness 119903119908is the radius of the
wellbore119861119900is the volume factor of the reservoir fluid 119878
119911is the
effective skin due to vertical flow 1198861and 119886
2are the coefficient
and have respectively the values of 0611 and 1083 in the earlytime of transient influx
For gas reservoir the expression of the transient inflowis a bit different from (16) the analytical solution for oilreservoir proposed by van Kruijisdijk and Cox [6] Thecompressibility of gas decides the influx difference betweenoil and gas reservoirWe define the pseudopressure as follows
= 2int
119901
1199010
119901
120583
119892(119901)119885 (119901)
119889119901 (19)
where 119901
0is the known pressure for reference 120583
119892is the gas
viscosity and 119885 is the compressibility factor of the gas Thenthe total influx rates of gas reservoir during underbalanceddrilling can be given
119902
119905119900119905(119905) = int
119905
0
119906
119901int
119905
120591
120597 (
119903119890119904minus
119908(120577))
120597120577
119902
119908119906(Θ 119905 minus 120577) 119889120577 119889120591
(20)
Analogously we rewrite the analytical expression of 119902119908119906
forgas reservoir in the following manner
119902
119908119906(119905) =
120587119896ℎ
119861
119892
119885
119904119888119879
119904119888120588
119892119904119888
119901
119904119888119879
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(21)
where the subscript denotes the standard state
5 Methodology of EstimatingReservoir Characterization
After establishing datamonitoring system in real time a tran-sient liquid-gas two-phase flow model in wellbore and wellinflux model during drilling have been derived Hereuntowe have reliable data acquisition approach and theoreticalmodel for reservoir characterization In this section let usfocus on specific approach to estimate reservoir properties Atfirst we will propose a new methodology to acquire reservoirpore pressure and then discuss how to extract the reservoirpermeability profiles during drilling
51 Reservoir Pore Pressure Inspired by the interestingmethodology of identifying reservoir pore pressure proposedby Kneissl [12] a new improved method of testing reservoirpore pressure is developed using different testing procedureavoiding the uncertainties affected by variations of fluid flowbehavior in the annulus sections and unpredictable inflowof new added zones It is noted that the idea of identifyingreservoir pore pressure by actively fluctuating the bottomhole pressure is still the key kernel thought of our methodFocusing on the new methodology a principal assumptionhas to be made that the reservoir drilled consists of differentzones with constant formation pressure coefficient whichcorresponds with the most common circumstances Withthe continuous pressure system assumption it is easy to
8 Journal of Applied Mathematics
obtain reservoir pore pressure of each zone by extracting thereservoir pressure coefficient when the reservoir is openedThis greatly simplifies the procedure of pore pressure testand avoids complex mathematical computation usually usedin other methods To eliminate the uncertainties of estimateresults introduced by continuous inflow of new zones it isneeded to stop drilling but keep circulation to begin thetesting operation when the first reservoir zone was openedwhich is the difference from Kneisslrsquos method in testingprocedure Taking into account the fact that only the first zonewas opened in the testing operation the transient inflow ofwell can be given by
119902
119908(119905) =
2120587119896ℎ (119901
119903119890119904minus 119901
119908(119905))
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(22)
It can be rewritten as
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(23)
At very short time the expression reduces to the followingmanner
lim119905rarr0
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
= lim119905rarr0
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911
(24)
which is entirely independent of the time and the downside of the equation can be considered constant for a givenreservoir It also can be interpreted that the transient inflowof well has a significant negative linear correlation with thepressure at bottom hole in the earliest hours of inflow Forthe inflow of well to become zero the reservoir pore pressureis approached by the pressure at bottom hole Thence wecan identify the reservoir pore pressure by searching forthe linear correlation between the inflow and pressure atbottom at the early stage of transient inflow This processis performed by introducing artificially fluctuations in thebottom hole pressure and by measuring the inflow rates andbottom hole pressure based on the real-time data monitoringsystem For aerated drilling the bottom hole pressure can beestimated using the transient wellbore flowmodel mentionedin this paper Figure 4 illustrates some details concerninghow to extract the reservoir pore pressure Here linear fittingof some measurement points is used to identify the linearcorrelation between thewell inflow and bottomhole pressureand the reservoir pore pressure can be read at the crossingof the best-fit regression line and the horizontal axis Forthe reliability of test results the number of testing pointsshould not be less than three Fluctuations of the bottom holepressure can be introduced by managing the choke valvechanging gas injection rates or pump rates To eliminatethe effects of variations of fluid flow in the wellbore onthe estimated results it is necessary to leave enough timeto capture relative steady inflow rates for each fluctuating
High
High
Low
0
qw
pw
Testing dataBest-fit regression line
Reservoir pressure
Figure 4 Reservoir pore pressure test by introducing fluctuation atthe bottom hole pressure
operation and the time needed lasts for a few minutes ormore than one hour which depends on well depth the typeof operations introducing the fluctuation in the bottom holepressure reservoir characteristics such as permeability andformation fluid properties and so on
Having acquired the reservoir pore pressure of the firstzone when the reservoir is opened the reservoir pressurecoefficient and pressure of subsequent zones can be obtainedduring drilling using a simple formula For the case wheremore than one reservoir with different pressure system wasdrilled new testing procedure should be repeated when newreservoir was opened The only difference is that the inflowmeasurements consist of the transient inflow response ofthe former reservoir and the transient well inflow of newreservoirrsquos first zone Here necessarymathematical treatmentof the inflow measurements is needed
52 Permeability Profiles To determine the reservoir perme-ability we make the simplifying assumption that the perme-ability is constant in specified zones of the well Transientinflux from each reservoir zone with different permeabilityat the time of interest constitutes the total production rates ofthewell which can be got from the real-time data acquisitionssystem The analytical expressions of total production ratesand unit-underbalance response of each zone which arerelated to the permeability have been established in the lastsection of this paper The reservoir pore pressure of eachreservoir zone can be calculated after testing the reservoirpressure coefficient just when the reservoir was opened Itis assumed that the porosity reservoir height and otherreservoir parameters apart from permeability are constantand known Theoretically the permeability of each reservoirzone can be easily determined using (18) and (21) Unfor-tunately the analytical expressions of the total productionrates are given in integral form which results in that theycannot readily be implemented in spreadsheet and calculator
Journal of Applied Mathematics 9
applications To facilitate the calculation a full discretizationof the total production rates formula is given instead of theintegral form in the following manner
119902
119905119900119905(119905) = 119906
119901(119901
119903119890119904minus 119901
119908)
119899=119905Δ119905
sum
119894=1
119902
119908119906119894(Θ
119894 119905 minus 119905
119894) Δ119905 (25)
where Δ119905 represents the time needed to penetrate througha reservoir element which is constant with the assumptionof the fixed penetration rate 119902
119908119906119894(Θ
119894 119905 minus 119905
119894) denotes unit-
underbalanced inflow of unit reservoir segment from zone 119894and 119905
119894denotes the time the wellbore reaches zone 119894 The value
of 119902119908119906119894
(Θ
119894 119905 minus 119905
119894) for nonpositive arguments is set equal to 0
The above discretization equation was given on the basisof a reasonable assumption that we have a constant underbal-ance which is realistic and is of engineering significance forunderbalanced drilling of a horizontal well
First we discuss how to extract the permeability of the1st reservoir zone The total production rates from the real-time monitoring system at the first time step when reservoiris opened can be simply considered to be the influx from thefirst zone Then we have the following formula
119902
119905119900119905(119905
1) = 119902
1199081(119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) 119902
1199081199061(Θ
1 119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
1ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896Δ119905120601120583119888119903
2
119908
(26)
Solving the equation above 1198961 the permeability of the 1st
reservoir zone can be given as follows
119896
1= (119898
2119902
1199081(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
1199081
(119905
1) Δ119905 +
119902
1199081(119905
1) 119878
119911
119898
1
)
2
(27)
where
119898
1=
2119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) ℎ119886
1
120583119861
119900119903
119908
119898
2=
119886
2
2119898
1119903
119908
radic120601120583119888
(28)
Analogously well influx from the reservoir element 119894 canbe given
119902
119908119894(119905
1)
= 119902
119905119900119905(119905
119894) minus
119894minus1
sum
119899=1
119902
119908119899(119905
119894minus119899)
= 119902
119905119900119905(119905
119894) minus 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
119894minus1
sum
119899=1
119902
119908119906119899(119905
119894minus 119905
119899)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
119894ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896
119894Δ119905120601120583119888119903
2
119908
(29)
where 119902tot(119905119894) represents the total production rates of the wellat time 119905
119894when the reservoir element is opened 119902
119908119906119899(119905
119894minus 119905
119899)
denotes the unit-underbalance transient influx response ofunit thickness reservoir from reservoir zone 119899 at time 119905
119894and
can be given using (21)Then we can extract the permeability of the reservoir
zone 119894 by
119896
119894= (119898
2119902
119908119894(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
119908119894
(119905
1) Δ119905 +
119902
119908119894(119905
1) 119878
119911
119898
1
)
2
(30)
Using the methodology the permeability of a set ofreservoir zones can be successively extracted as the reservoiris being penetrated by a horizontal well To facilitate theprecise calculation and estimate permeability profiles in timea computer procedure was used in this paper The success ofreservoir permeability estimation profits from reliable real-time data monitoring system advanced wellbore flow andreservoir model and an innovative reservoir pore pressuretest approach
6 Results and Discussion
The methodology presented in this paper has been used toidentify the reservoir pore pressure and permeability profilesof approximately 10 wells during underbalanced drilling inChina In order to illustrate the above approach in detail anactual horizontal well and gas reservoir are considered in thissection It is appropriate to emphasize that the well picked ascase study is the first successful application of this method-ology More exhaustive data and offset information from thiswell facilitate the effectiveness evaluation of this methodThereservoir dealt with here is the Ordovician carbonate gasreservoir with natural fractures as the dominant gas storagespaces and flowing channels To avoid lost circulation andformation damage the well is drilled underbalanced usingthe aerated clay-free drilling fluid while this is also beneficialfor well control Here nitrogen is used as the injection gasThe hole geometry and drilling assembly of this well wereillustrated in Figure 5 Some basic parameters for reservoirand drilling fluid used in reservoir characterization wereshown in Table 1
61 Data Acquisition in Real Time The real-time data mon-itoring system for aerated drilling presented in this paperwas used to acquire basic data for reservoir characterizationin real time The application of this system guaranteesthat the indispensable parameters are accurate and timelywhichmakes it possible to identify reservoir characterizationDuring drilling this system succeed in the integration of thedata from compound logging and our sensitive measuringinstruments and the digital microwave transmission wasproved to be realizable and reliable to deliver wirelesslydata Some typical acquired measurements plotted againsttime are shown in Figures 6ndash10 In order to illustrate thetransient behavior for different parameters the measuringtime for different parameters in figures differs The standpipe
10 Journal of Applied Mathematics
Drill bit
Cement
Casing
Drill strings
Wellhead
Bottom holeBarefoot interval
Annulus
Protective casing interval
Drill strings size
Diameter 01524m
Diameter 01524mDepth 4000ndash4960m
Inner diameter 022m
Outside diameter 01397mInner diameter 01214m
Outside diameter 00889mInner diameter 00702m
Outside diameter 00889mInner diameter 00381m
Depth 0ndash
Depth 0ndash1800m
Depth 1800ndash4930m
Depth 4930ndash4960m
4000m
Figure 5 The hole geometry and drilling assembly of the well
Table 1 Basic parameters for reservoir and drilling fluid used inreservoir characterization
Depth evaluation of the reservoir m 4156Reservoir thickness m 15Porosity 12Reservoir fluid volume factor m3stdm3 0008Reservoir fluid viscosity mPasdots 0035Reservoir compressibility Paminus1 116 times 10minus9
Reservoir fluid compressibility Paminus1 1177 times 10minus9
Geothermal temperature Ksdotmminus1 003Drilling fluid density at standard conditions gsdotcmminus3 104Drilling fluid viscosity at standard conditions mPasdots 20Injection gas specific gravity 1 097Injection gas viscosity at standard conditions mPasdots 0019
pressure and casing pressure for different time are plottedrespectively in Figures 6 and 7 It can be seen that thetransient fluctuations of standpipe pressure are more acutethan that of casing pressure In general this difference canbe aroused by unsteady drilling fluid and gas injection checkcalve measuring apparatus installed along drill string anddrill string vibrationThe casing pressure changing with timein Figure 7 indicates the different outlet gas rates or variedchoke opening Figure 8 shows the drilling fluid density asa function of time for outlet and injection respectivelyContrary to the standard drilling operations more accurateand automatic measurements of drilling fluid density can beobtained in real time utilizing instrumented standpipe andseparator drilling fluid outlet pipe using different pressure
2030 2118 2207 2254 234110
11
12
13
14
15
16
17
18
Stan
dpip
e pre
ssur
e (M
Pa)
Time1930
Figure 6 Data acquisitionmdashstandpipe pressure data versus time(2010-9-27)
1151 1342 1527 1715 1901 2052 2230250
275
300
325
350
375
400Ca
sing
pres
sure
(MPa
)
Time1000
Figure 7 Data acquisitionmdashcasing pressure data versus time (2010-9-27)
transducers not measured manually in intervals of 15 min-utes It is noted that the outlet drilling fluid density is slightlylower than that of injection fluid and fluctuates wildly Thistransient behavior of outlet drilling fluid density occurs as aresult of varied outlet gas rates and nonthorough degassing ofdrilling fluid In this study we monitor the total hydrocarboncontent of outlet gas and outlet gas rates to acquire thereservoir gas inflow rates in real timeThemeasured outlet gasrates and reservoir gas inflow rates are presented in Figure 9The real-time reservoir gas inflow rates absolutely criticalfor reservoir characterization are calculated using the outletgas rates and total hydrocarbon content in time of interestas shown in Figure 10 In sum the application of the newreal-time data monitoring system in this well helps drillingcontractor with good underbalanced drilling operations and
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
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Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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Stochastic AnalysisInternational Journal of
8 Journal of Applied Mathematics
obtain reservoir pore pressure of each zone by extracting thereservoir pressure coefficient when the reservoir is openedThis greatly simplifies the procedure of pore pressure testand avoids complex mathematical computation usually usedin other methods To eliminate the uncertainties of estimateresults introduced by continuous inflow of new zones it isneeded to stop drilling but keep circulation to begin thetesting operation when the first reservoir zone was openedwhich is the difference from Kneisslrsquos method in testingprocedure Taking into account the fact that only the first zonewas opened in the testing operation the transient inflow ofwell can be given by
119902
119908(119905) =
2120587119896ℎ (119901
119903119890119904minus 119901
119908(119905))
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(22)
It can be rewritten as
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
(23)
At very short time the expression reduces to the followingmanner
lim119905rarr0
119902
119908(119905)
119901
119903119890119904minus 119901
119908(119905)
= lim119905rarr0
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896119905120601120583119888119903
2
119908
=
2120587119896ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911
(24)
which is entirely independent of the time and the downside of the equation can be considered constant for a givenreservoir It also can be interpreted that the transient inflowof well has a significant negative linear correlation with thepressure at bottom hole in the earliest hours of inflow Forthe inflow of well to become zero the reservoir pore pressureis approached by the pressure at bottom hole Thence wecan identify the reservoir pore pressure by searching forthe linear correlation between the inflow and pressure atbottom at the early stage of transient inflow This processis performed by introducing artificially fluctuations in thebottom hole pressure and by measuring the inflow rates andbottom hole pressure based on the real-time data monitoringsystem For aerated drilling the bottom hole pressure can beestimated using the transient wellbore flowmodel mentionedin this paper Figure 4 illustrates some details concerninghow to extract the reservoir pore pressure Here linear fittingof some measurement points is used to identify the linearcorrelation between thewell inflow and bottomhole pressureand the reservoir pore pressure can be read at the crossingof the best-fit regression line and the horizontal axis Forthe reliability of test results the number of testing pointsshould not be less than three Fluctuations of the bottom holepressure can be introduced by managing the choke valvechanging gas injection rates or pump rates To eliminatethe effects of variations of fluid flow in the wellbore onthe estimated results it is necessary to leave enough timeto capture relative steady inflow rates for each fluctuating
High
High
Low
0
qw
pw
Testing dataBest-fit regression line
Reservoir pressure
Figure 4 Reservoir pore pressure test by introducing fluctuation atthe bottom hole pressure
operation and the time needed lasts for a few minutes ormore than one hour which depends on well depth the typeof operations introducing the fluctuation in the bottom holepressure reservoir characteristics such as permeability andformation fluid properties and so on
Having acquired the reservoir pore pressure of the firstzone when the reservoir is opened the reservoir pressurecoefficient and pressure of subsequent zones can be obtainedduring drilling using a simple formula For the case wheremore than one reservoir with different pressure system wasdrilled new testing procedure should be repeated when newreservoir was opened The only difference is that the inflowmeasurements consist of the transient inflow response ofthe former reservoir and the transient well inflow of newreservoirrsquos first zone Here necessarymathematical treatmentof the inflow measurements is needed
52 Permeability Profiles To determine the reservoir perme-ability we make the simplifying assumption that the perme-ability is constant in specified zones of the well Transientinflux from each reservoir zone with different permeabilityat the time of interest constitutes the total production rates ofthewell which can be got from the real-time data acquisitionssystem The analytical expressions of total production ratesand unit-underbalance response of each zone which arerelated to the permeability have been established in the lastsection of this paper The reservoir pore pressure of eachreservoir zone can be calculated after testing the reservoirpressure coefficient just when the reservoir was opened Itis assumed that the porosity reservoir height and otherreservoir parameters apart from permeability are constantand known Theoretically the permeability of each reservoirzone can be easily determined using (18) and (21) Unfor-tunately the analytical expressions of the total productionrates are given in integral form which results in that theycannot readily be implemented in spreadsheet and calculator
Journal of Applied Mathematics 9
applications To facilitate the calculation a full discretizationof the total production rates formula is given instead of theintegral form in the following manner
119902
119905119900119905(119905) = 119906
119901(119901
119903119890119904minus 119901
119908)
119899=119905Δ119905
sum
119894=1
119902
119908119906119894(Θ
119894 119905 minus 119905
119894) Δ119905 (25)
where Δ119905 represents the time needed to penetrate througha reservoir element which is constant with the assumptionof the fixed penetration rate 119902
119908119906119894(Θ
119894 119905 minus 119905
119894) denotes unit-
underbalanced inflow of unit reservoir segment from zone 119894and 119905
119894denotes the time the wellbore reaches zone 119894 The value
of 119902119908119906119894
(Θ
119894 119905 minus 119905
119894) for nonpositive arguments is set equal to 0
The above discretization equation was given on the basisof a reasonable assumption that we have a constant underbal-ance which is realistic and is of engineering significance forunderbalanced drilling of a horizontal well
First we discuss how to extract the permeability of the1st reservoir zone The total production rates from the real-time monitoring system at the first time step when reservoiris opened can be simply considered to be the influx from thefirst zone Then we have the following formula
119902
119905119900119905(119905
1) = 119902
1199081(119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) 119902
1199081199061(Θ
1 119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
1ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896Δ119905120601120583119888119903
2
119908
(26)
Solving the equation above 1198961 the permeability of the 1st
reservoir zone can be given as follows
119896
1= (119898
2119902
1199081(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
1199081
(119905
1) Δ119905 +
119902
1199081(119905
1) 119878
119911
119898
1
)
2
(27)
where
119898
1=
2119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) ℎ119886
1
120583119861
119900119903
119908
119898
2=
119886
2
2119898
1119903
119908
radic120601120583119888
(28)
Analogously well influx from the reservoir element 119894 canbe given
119902
119908119894(119905
1)
= 119902
119905119900119905(119905
119894) minus
119894minus1
sum
119899=1
119902
119908119899(119905
119894minus119899)
= 119902
119905119900119905(119905
119894) minus 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
119894minus1
sum
119899=1
119902
119908119906119899(119905
119894minus 119905
119899)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
119894ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896
119894Δ119905120601120583119888119903
2
119908
(29)
where 119902tot(119905119894) represents the total production rates of the wellat time 119905
119894when the reservoir element is opened 119902
119908119906119899(119905
119894minus 119905
119899)
denotes the unit-underbalance transient influx response ofunit thickness reservoir from reservoir zone 119899 at time 119905
119894and
can be given using (21)Then we can extract the permeability of the reservoir
zone 119894 by
119896
119894= (119898
2119902
119908119894(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
119908119894
(119905
1) Δ119905 +
119902
119908119894(119905
1) 119878
119911
119898
1
)
2
(30)
Using the methodology the permeability of a set ofreservoir zones can be successively extracted as the reservoiris being penetrated by a horizontal well To facilitate theprecise calculation and estimate permeability profiles in timea computer procedure was used in this paper The success ofreservoir permeability estimation profits from reliable real-time data monitoring system advanced wellbore flow andreservoir model and an innovative reservoir pore pressuretest approach
6 Results and Discussion
The methodology presented in this paper has been used toidentify the reservoir pore pressure and permeability profilesof approximately 10 wells during underbalanced drilling inChina In order to illustrate the above approach in detail anactual horizontal well and gas reservoir are considered in thissection It is appropriate to emphasize that the well picked ascase study is the first successful application of this method-ology More exhaustive data and offset information from thiswell facilitate the effectiveness evaluation of this methodThereservoir dealt with here is the Ordovician carbonate gasreservoir with natural fractures as the dominant gas storagespaces and flowing channels To avoid lost circulation andformation damage the well is drilled underbalanced usingthe aerated clay-free drilling fluid while this is also beneficialfor well control Here nitrogen is used as the injection gasThe hole geometry and drilling assembly of this well wereillustrated in Figure 5 Some basic parameters for reservoirand drilling fluid used in reservoir characterization wereshown in Table 1
61 Data Acquisition in Real Time The real-time data mon-itoring system for aerated drilling presented in this paperwas used to acquire basic data for reservoir characterizationin real time The application of this system guaranteesthat the indispensable parameters are accurate and timelywhichmakes it possible to identify reservoir characterizationDuring drilling this system succeed in the integration of thedata from compound logging and our sensitive measuringinstruments and the digital microwave transmission wasproved to be realizable and reliable to deliver wirelesslydata Some typical acquired measurements plotted againsttime are shown in Figures 6ndash10 In order to illustrate thetransient behavior for different parameters the measuringtime for different parameters in figures differs The standpipe
10 Journal of Applied Mathematics
Drill bit
Cement
Casing
Drill strings
Wellhead
Bottom holeBarefoot interval
Annulus
Protective casing interval
Drill strings size
Diameter 01524m
Diameter 01524mDepth 4000ndash4960m
Inner diameter 022m
Outside diameter 01397mInner diameter 01214m
Outside diameter 00889mInner diameter 00702m
Outside diameter 00889mInner diameter 00381m
Depth 0ndash
Depth 0ndash1800m
Depth 1800ndash4930m
Depth 4930ndash4960m
4000m
Figure 5 The hole geometry and drilling assembly of the well
Table 1 Basic parameters for reservoir and drilling fluid used inreservoir characterization
Depth evaluation of the reservoir m 4156Reservoir thickness m 15Porosity 12Reservoir fluid volume factor m3stdm3 0008Reservoir fluid viscosity mPasdots 0035Reservoir compressibility Paminus1 116 times 10minus9
Reservoir fluid compressibility Paminus1 1177 times 10minus9
Geothermal temperature Ksdotmminus1 003Drilling fluid density at standard conditions gsdotcmminus3 104Drilling fluid viscosity at standard conditions mPasdots 20Injection gas specific gravity 1 097Injection gas viscosity at standard conditions mPasdots 0019
pressure and casing pressure for different time are plottedrespectively in Figures 6 and 7 It can be seen that thetransient fluctuations of standpipe pressure are more acutethan that of casing pressure In general this difference canbe aroused by unsteady drilling fluid and gas injection checkcalve measuring apparatus installed along drill string anddrill string vibrationThe casing pressure changing with timein Figure 7 indicates the different outlet gas rates or variedchoke opening Figure 8 shows the drilling fluid density asa function of time for outlet and injection respectivelyContrary to the standard drilling operations more accurateand automatic measurements of drilling fluid density can beobtained in real time utilizing instrumented standpipe andseparator drilling fluid outlet pipe using different pressure
2030 2118 2207 2254 234110
11
12
13
14
15
16
17
18
Stan
dpip
e pre
ssur
e (M
Pa)
Time1930
Figure 6 Data acquisitionmdashstandpipe pressure data versus time(2010-9-27)
1151 1342 1527 1715 1901 2052 2230250
275
300
325
350
375
400Ca
sing
pres
sure
(MPa
)
Time1000
Figure 7 Data acquisitionmdashcasing pressure data versus time (2010-9-27)
transducers not measured manually in intervals of 15 min-utes It is noted that the outlet drilling fluid density is slightlylower than that of injection fluid and fluctuates wildly Thistransient behavior of outlet drilling fluid density occurs as aresult of varied outlet gas rates and nonthorough degassing ofdrilling fluid In this study we monitor the total hydrocarboncontent of outlet gas and outlet gas rates to acquire thereservoir gas inflow rates in real timeThemeasured outlet gasrates and reservoir gas inflow rates are presented in Figure 9The real-time reservoir gas inflow rates absolutely criticalfor reservoir characterization are calculated using the outletgas rates and total hydrocarbon content in time of interestas shown in Figure 10 In sum the application of the newreal-time data monitoring system in this well helps drillingcontractor with good underbalanced drilling operations and
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
Journal of Applied Mathematics 9
applications To facilitate the calculation a full discretizationof the total production rates formula is given instead of theintegral form in the following manner
119902
119905119900119905(119905) = 119906
119901(119901
119903119890119904minus 119901
119908)
119899=119905Δ119905
sum
119894=1
119902
119908119906119894(Θ
119894 119905 minus 119905
119894) Δ119905 (25)
where Δ119905 represents the time needed to penetrate througha reservoir element which is constant with the assumptionof the fixed penetration rate 119902
119908119906119894(Θ
119894 119905 minus 119905
119894) denotes unit-
underbalanced inflow of unit reservoir segment from zone 119894and 119905
119894denotes the time the wellbore reaches zone 119894 The value
of 119902119908119906119894
(Θ
119894 119905 minus 119905
119894) for nonpositive arguments is set equal to 0
The above discretization equation was given on the basisof a reasonable assumption that we have a constant underbal-ance which is realistic and is of engineering significance forunderbalanced drilling of a horizontal well
First we discuss how to extract the permeability of the1st reservoir zone The total production rates from the real-time monitoring system at the first time step when reservoiris opened can be simply considered to be the influx from thefirst zone Then we have the following formula
119902
119905119900119905(119905
1) = 119902
1199081(119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) 119902
1199081199061(Θ
1 119905
1)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
1ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896Δ119905120601120583119888119903
2
119908
(26)
Solving the equation above 1198961 the permeability of the 1st
reservoir zone can be given as follows
119896
1= (119898
2119902
1199081(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
1199081
(119905
1) Δ119905 +
119902
1199081(119905
1) 119878
119911
119898
1
)
2
(27)
where
119898
1=
2119906
119901Δ119905 (119901
119903119890119904minus 119901
119908) ℎ119886
1
120583119861
119900119903
119908
119898
2=
119886
2
2119898
1119903
119908
radic120601120583119888
(28)
Analogously well influx from the reservoir element 119894 canbe given
119902
119908119894(119905
1)
= 119902
119905119900119905(119905
119894) minus
119894minus1
sum
119899=1
119902
119908119899(119905
119894minus119899)
= 119902
119905119900119905(119905
119894) minus 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
119894minus1
sum
119899=1
119902
119908119906119899(119905
119894minus 119905
119899)
= 119906
119901Δ119905 (119901
119903119890119904minus 119901
119908)
2120587119896
119894ℎ
120583119861
119900
119886
1 (120587119903
119908)
119878
119911+ 119886
2
radic119896
119894Δ119905120601120583119888119903
2
119908
(29)
where 119902tot(119905119894) represents the total production rates of the wellat time 119905
119894when the reservoir element is opened 119902
119908119906119899(119905
119894minus 119905
119899)
denotes the unit-underbalance transient influx response ofunit thickness reservoir from reservoir zone 119899 at time 119905
119894and
can be given using (21)Then we can extract the permeability of the reservoir
zone 119894 by
119896
119894= (119898
2119902
119908119894(119905
1)radicΔ119905 +
radic119898
2
2
119902
2
119908119894
(119905
1) Δ119905 +
119902
119908119894(119905
1) 119878
119911
119898
1
)
2
(30)
Using the methodology the permeability of a set ofreservoir zones can be successively extracted as the reservoiris being penetrated by a horizontal well To facilitate theprecise calculation and estimate permeability profiles in timea computer procedure was used in this paper The success ofreservoir permeability estimation profits from reliable real-time data monitoring system advanced wellbore flow andreservoir model and an innovative reservoir pore pressuretest approach
6 Results and Discussion
The methodology presented in this paper has been used toidentify the reservoir pore pressure and permeability profilesof approximately 10 wells during underbalanced drilling inChina In order to illustrate the above approach in detail anactual horizontal well and gas reservoir are considered in thissection It is appropriate to emphasize that the well picked ascase study is the first successful application of this method-ology More exhaustive data and offset information from thiswell facilitate the effectiveness evaluation of this methodThereservoir dealt with here is the Ordovician carbonate gasreservoir with natural fractures as the dominant gas storagespaces and flowing channels To avoid lost circulation andformation damage the well is drilled underbalanced usingthe aerated clay-free drilling fluid while this is also beneficialfor well control Here nitrogen is used as the injection gasThe hole geometry and drilling assembly of this well wereillustrated in Figure 5 Some basic parameters for reservoirand drilling fluid used in reservoir characterization wereshown in Table 1
61 Data Acquisition in Real Time The real-time data mon-itoring system for aerated drilling presented in this paperwas used to acquire basic data for reservoir characterizationin real time The application of this system guaranteesthat the indispensable parameters are accurate and timelywhichmakes it possible to identify reservoir characterizationDuring drilling this system succeed in the integration of thedata from compound logging and our sensitive measuringinstruments and the digital microwave transmission wasproved to be realizable and reliable to deliver wirelesslydata Some typical acquired measurements plotted againsttime are shown in Figures 6ndash10 In order to illustrate thetransient behavior for different parameters the measuringtime for different parameters in figures differs The standpipe
10 Journal of Applied Mathematics
Drill bit
Cement
Casing
Drill strings
Wellhead
Bottom holeBarefoot interval
Annulus
Protective casing interval
Drill strings size
Diameter 01524m
Diameter 01524mDepth 4000ndash4960m
Inner diameter 022m
Outside diameter 01397mInner diameter 01214m
Outside diameter 00889mInner diameter 00702m
Outside diameter 00889mInner diameter 00381m
Depth 0ndash
Depth 0ndash1800m
Depth 1800ndash4930m
Depth 4930ndash4960m
4000m
Figure 5 The hole geometry and drilling assembly of the well
Table 1 Basic parameters for reservoir and drilling fluid used inreservoir characterization
Depth evaluation of the reservoir m 4156Reservoir thickness m 15Porosity 12Reservoir fluid volume factor m3stdm3 0008Reservoir fluid viscosity mPasdots 0035Reservoir compressibility Paminus1 116 times 10minus9
Reservoir fluid compressibility Paminus1 1177 times 10minus9
Geothermal temperature Ksdotmminus1 003Drilling fluid density at standard conditions gsdotcmminus3 104Drilling fluid viscosity at standard conditions mPasdots 20Injection gas specific gravity 1 097Injection gas viscosity at standard conditions mPasdots 0019
pressure and casing pressure for different time are plottedrespectively in Figures 6 and 7 It can be seen that thetransient fluctuations of standpipe pressure are more acutethan that of casing pressure In general this difference canbe aroused by unsteady drilling fluid and gas injection checkcalve measuring apparatus installed along drill string anddrill string vibrationThe casing pressure changing with timein Figure 7 indicates the different outlet gas rates or variedchoke opening Figure 8 shows the drilling fluid density asa function of time for outlet and injection respectivelyContrary to the standard drilling operations more accurateand automatic measurements of drilling fluid density can beobtained in real time utilizing instrumented standpipe andseparator drilling fluid outlet pipe using different pressure
2030 2118 2207 2254 234110
11
12
13
14
15
16
17
18
Stan
dpip
e pre
ssur
e (M
Pa)
Time1930
Figure 6 Data acquisitionmdashstandpipe pressure data versus time(2010-9-27)
1151 1342 1527 1715 1901 2052 2230250
275
300
325
350
375
400Ca
sing
pres
sure
(MPa
)
Time1000
Figure 7 Data acquisitionmdashcasing pressure data versus time (2010-9-27)
transducers not measured manually in intervals of 15 min-utes It is noted that the outlet drilling fluid density is slightlylower than that of injection fluid and fluctuates wildly Thistransient behavior of outlet drilling fluid density occurs as aresult of varied outlet gas rates and nonthorough degassing ofdrilling fluid In this study we monitor the total hydrocarboncontent of outlet gas and outlet gas rates to acquire thereservoir gas inflow rates in real timeThemeasured outlet gasrates and reservoir gas inflow rates are presented in Figure 9The real-time reservoir gas inflow rates absolutely criticalfor reservoir characterization are calculated using the outletgas rates and total hydrocarbon content in time of interestas shown in Figure 10 In sum the application of the newreal-time data monitoring system in this well helps drillingcontractor with good underbalanced drilling operations and
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
10 Journal of Applied Mathematics
Drill bit
Cement
Casing
Drill strings
Wellhead
Bottom holeBarefoot interval
Annulus
Protective casing interval
Drill strings size
Diameter 01524m
Diameter 01524mDepth 4000ndash4960m
Inner diameter 022m
Outside diameter 01397mInner diameter 01214m
Outside diameter 00889mInner diameter 00702m
Outside diameter 00889mInner diameter 00381m
Depth 0ndash
Depth 0ndash1800m
Depth 1800ndash4930m
Depth 4930ndash4960m
4000m
Figure 5 The hole geometry and drilling assembly of the well
Table 1 Basic parameters for reservoir and drilling fluid used inreservoir characterization
Depth evaluation of the reservoir m 4156Reservoir thickness m 15Porosity 12Reservoir fluid volume factor m3stdm3 0008Reservoir fluid viscosity mPasdots 0035Reservoir compressibility Paminus1 116 times 10minus9
Reservoir fluid compressibility Paminus1 1177 times 10minus9
Geothermal temperature Ksdotmminus1 003Drilling fluid density at standard conditions gsdotcmminus3 104Drilling fluid viscosity at standard conditions mPasdots 20Injection gas specific gravity 1 097Injection gas viscosity at standard conditions mPasdots 0019
pressure and casing pressure for different time are plottedrespectively in Figures 6 and 7 It can be seen that thetransient fluctuations of standpipe pressure are more acutethan that of casing pressure In general this difference canbe aroused by unsteady drilling fluid and gas injection checkcalve measuring apparatus installed along drill string anddrill string vibrationThe casing pressure changing with timein Figure 7 indicates the different outlet gas rates or variedchoke opening Figure 8 shows the drilling fluid density asa function of time for outlet and injection respectivelyContrary to the standard drilling operations more accurateand automatic measurements of drilling fluid density can beobtained in real time utilizing instrumented standpipe andseparator drilling fluid outlet pipe using different pressure
2030 2118 2207 2254 234110
11
12
13
14
15
16
17
18
Stan
dpip
e pre
ssur
e (M
Pa)
Time1930
Figure 6 Data acquisitionmdashstandpipe pressure data versus time(2010-9-27)
1151 1342 1527 1715 1901 2052 2230250
275
300
325
350
375
400Ca
sing
pres
sure
(MPa
)
Time1000
Figure 7 Data acquisitionmdashcasing pressure data versus time (2010-9-27)
transducers not measured manually in intervals of 15 min-utes It is noted that the outlet drilling fluid density is slightlylower than that of injection fluid and fluctuates wildly Thistransient behavior of outlet drilling fluid density occurs as aresult of varied outlet gas rates and nonthorough degassing ofdrilling fluid In this study we monitor the total hydrocarboncontent of outlet gas and outlet gas rates to acquire thereservoir gas inflow rates in real timeThemeasured outlet gasrates and reservoir gas inflow rates are presented in Figure 9The real-time reservoir gas inflow rates absolutely criticalfor reservoir characterization are calculated using the outletgas rates and total hydrocarbon content in time of interestas shown in Figure 10 In sum the application of the newreal-time data monitoring system in this well helps drillingcontractor with good underbalanced drilling operations and
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
Journal of Applied Mathematics 11
1320 1340 1400 1420 1440 1500093
096
099
102
105
108
111
Outlet drilling fluid densitiesInjection drilling fluid densities
Time1300
Dril
ling
fluid
den
sitie
s(gmiddot
cmminus3)
Figure 8 Data acquisitionmdashdrilling fluid density data versus time(2010-9-25)
0230 0454 0716 0933 11530
500
1000
1500
2000
2500
000Time
Outlet gas ratesGas inflow rates
Gas
rate
s(m
3middoth
minus1)
Figure 9 Data acquisitionmdashoutlet gas rates and gas inflow ratesdata versus time (2010-9-25)
provides accurate and more complete data set in real time forreservoir characterization during drilling
62 Reservoir Characterization In this paper the reservoircharacterization we are interested in refers to the reservoirpore pressure and reservoir permeability It is assumed thatthe reservoir dealt with here consists of a number of differentzones each 1m in thickness With each zone the reservoirpore pressure and permeability are constant In this sectionwe discuss the details of identifying the reservoir porepressure and permeability and their comparison with theactual data
230 454 716 933 115320
25
30
35
40
45
Tota
l hyd
roca
rbon
cont
ent (
)
Time000
Figure 10 Data acquisitionmdashtotal hydrocarbon content data versustime (2010-9-25)
For this well the reservoir was opened at the well depthof 4880m when visible gas inflow was detected for the firsttime And then we stopped drilling but kept circulation tobegin the reservoir pore pressure test procedure Here thefluctuations of the bottom hole pressure were introduced bymanually accommodating the choke valve without drillingfluid and gas injection changes After trying for some timesthree testing points with relative steady inflow lasts for morethan one hour were observed and illustrated in Figure 11 Foraerated drilling used in this well the bottom hole pressurefor three testing points can be estimated using the transientwellbore flow model The important input parameters in thewellbore flow simulation such as surface casing pressureoutlet gas and drilling fluid rates and outlet drilling fluiddensity were provided by the data monitoring system shownin Figure 1 in real time For the three testing points thetime-averaged gas inflow rates and bottom hole pressure andtheir best-fit regression line are plotted in Figure 12 With thefitted regression equation in Figure 12 it is easy to extractthe reservoir pore pressure for the first zone to be 4191MPaHaving known the vertical depth of 41397m when the testwas conducted the reservoir pressure coefficient can beobtained to be 1032 whichmeets very closely the actual valueof 103 obtained from well-test data after drilling The mea-sured inclination at the well depth of 4870 before beginningunderbalance drilling operation is 885∘ For aerated drillingthe hole inclination cannot bemeasured in real-time with theuse ofMWD It is appropriate tomake the assumption that wehave the same hole inclination for the underbalance drillinginterval with length of 80m Considering the case here thatthe reservoir with consistent pressure system was drilled by ahorizontal well it is easy to obtain the reservoir pore pressureprofile of thewell as shown in Figure 13 It is noted thatwe usethe actual reservoir pressure coefficient from well-test dataafter drilling Thus the good match between the estimatedreservoir pressure and actual data indicates the feasibility
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
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Stochastic AnalysisInternational Journal of
12 Journal of Applied Mathematics
003 102 157 251 346 440 533 6270
100
200
300
400
500
600
700
800
Steady inflow fornumber 3 point
Steady inflow fornumber 1 point
Time2302
Steady inflow fornumber 2 point
Gas
inflo
w ra
tes(
m3middoth
minus1)
Figure 11 Three segments of steady inflow obtained by introducingfluctuation at the bottom hole pressure
37 38 39 40 41 42 430
100
200
300
400
500
600
Pressure at bottom hole (MPa)Tested dataBest-fit regression line
Reservoir pressure
Gas
inflo
w ra
tes
y = minus12883x + 539944
R2 = 097611
(m3middotminminus1)
Figure 12 Gas inflow rates versus pressure at bottom hole and thebest-fit regression line
and reliability of the reservoir pressure test methodologypresented in this paper
Having obtained the reservoir pore pressure profile wecan extract the permeability of every zone from real-timemonitoring data using the methodology presented in thispaper To be candid this is not a simple event For everyzone complex mathematical computations are required toidentify permeability Some necessary mathematical equa-tions needed for computation have been mentioned in theabove section in this paper Basic parameters for reservoirand drilling fluid and the hole geometry and drilling assemblyof the well required for reservoir characterization havebeen given in Table 1 and Figure 5 respectively The datamonitoring system provided the real-time data required such
4880 4890 4900 4910 4920 4930 4940 4950 49604190
4191
4192
4193
4194
Rese
rvoi
r pre
ssur
e (M
Pa)
Well depth (m)
Figure 13 Reservoir pore pressure profile estimated using theimproved methodology
4880 4900 4920 4940 4960
001
01
1
10
100Pe
rmea
bilit
y (m
D)
Well depth (m)EstimateActual
1E minus 4
1E minus 3
Figure 14 A comparison between estimated and actual permeabil-ity profiles
as casing pressure injection and outlet gas rates injection andoutlet drilling fluid density and injection drilling fluid rateswhen performing reservoir characterization for every zoneThe estimated and actual permeability profiles are indicatedin Figure 14 and show a good agreement in magnitude onthe whole However we observe that there is a differencebetween the estimated and actual values of the permeabilityfor different zones In this example the actual permeabilitywas obtained using the multi-interval test after drillingand given in the form of average value for every intervalTo be different from the actual permeability the separatepermeability of every unit reservoir thickness was estimatedby dividing the reservoir into discrete zones with thickness of1m which is an outstanding originality of the methodology
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
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Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
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Journal of
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OptimizationJournal of
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CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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Decision SciencesAdvances in
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Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
Journal of Applied Mathematics 13
4880 4890 4900 4910 4920 4930 4940 4950 49600
1
2
3
4
5
UnderbalancePenetration rate
Well depth (m)
Und
erba
lanc
e (M
Pa)
0
2
4
6
8
10
Pene
trat
ion
rate
(mmiddoth
minus1)
Figure 15 Underbalance and penetration rates profiles
presented in this paper This is the major element causingthe difference between the estimated and actual permeabilityprofiles in Figure 14 Beyond this it is also observed that thequality of the reservoir characterization varies in differentzones The unconstant underbalance and penetration rateshown in Figure 15 might result in the difference In thispaper the mathematical expressions estimating the reservoirpermeability were derived with the constant underbalanceand penetration rate assumption The variable penetrationrates and underbalance cause the results that the estimatedpermeability are slight less accurate than those obtained withconstant penetration rates and underbalance [6] Besides theestimated results of the near zones opened subsequently arealso affected However the quality of the reservoir character-ization is still acceptable Low underbalance and penetrationrates are a benefit when performing characterization whichare also important for thewell control In the drilling practicethe penetration rates are easy to control but it is hard tokeep constant underbalance and penetration rate through allthe process and the only thing we could do was to restrictthe variation of the underbalance In order to validate thereservoir characterizationmethod proposed in this study thegas simulated outlet rates at a time when a high permeablezone was penetrated at a depth of 4907m were comparedin Figure 16 with the monitoring data The estimated perme-ability for different reservoir zones at depths from 4880m to4907m shown in Figure 14 was used to obtain the bottomhole gas influx rates in the simulation The real-time surfacecasing pressure measured using the data monitoring systembefore and after the zone of interest being opened was usedas the outlet boundary condition Some other importantparameters in the wellbore flow simulation were given inTable 2 The comparison is good showing that the estimatedpermeability is accurate and the transient well influx modeland multiphase flow model can be used to simulate thetransient wellbore flow during underbalanced drilling It isnoted that often there is no need to predict the outlet gas rateswhen performing the reservoir characterizationThe purpose
0 1000 2000 3000 4000 5000 6000 70000
640
1280
1920
2560
3200
Time (s)Simulated dataActual data
Gas
out
let r
ates
(m3middoth
minus1)
Figure 16 Simulated and actual gas outlet rates when the highpermeable zone at the depth of 4907m was penetrated
Table 2 Some required parameters used in the wellbore flowsimulation
Well depth of interest m 4907Injection drilling fluid density gsdotcmminus3 104Injection drilling fluid rates Lsdotsminus1 18Injection drilling fluid viscosity 20Gas injection rates m3
sdotminminus1 20Gas injection pressure MPa 154Gas injection temperature K 307Surface temperature K 300
of the outlet gas flow rates estimation in Figure 16 wasto reversely validate the reservoir characterization methodusing the estimated permeability profile In the standardprocedure of reservoir characterization the real-time outletgas rates and casing pressure measured using the datameasuring system are required in the transient wellbore flowsimulation as boundary outlet conditions to estimate thebottom hole pressure which is very important for extractingthe permeability of the reservoir zones
It is noted that a new multiphase flow model was appliedto simulate the wellbore flow behavior for aerated drillingwithout PWD data Effects of drilling fluid density behaviorand wellbore transfer were involved in the new model Thevalidity and practicability of new model are verified bygood agreement between simulated and monitoring resultsas shown in Figures 16 and 17 Here we discuss the effects ofdrilling fluid behavior and wellbore transfer on the wellboreflow pressure profile in the annulus During drilling opera-tions the annulus fluid being lower than the formation tem-perature receives heat from the formation In the meantimethe formation near the wellbore is also cooled by the flowingfluid in the annulusThe wellbore temperature in the annulushas a direct bearing on the drilling fluid density and the gas
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
14 Journal of Applied Mathematics
4880 4890 4900 4910 4920 4930 4940 4950 49600
5
10
15
20
25
Pres
sure
(MPa
)
Well depth (m)Surface casing pressureEstimated standpipe pressure Measured standpipe pressure
Figure 17 Time-averaged measured and estimated standpipe pres-sure and surface casing pressure when every zone were beingpenetrated
compressibility distributions along the annulus which arevery important for thewellbore flow simulation In this paperthe effects of the drilling fluid density were considered byinvoking the temperature and drilling fluid density using theanalytical models in (7) and (8) respectively The estimatedwellbore flow pressure profiles in the annulus for differentdrilling fluid circulation time were plotted in Figure 18 Itis noted that the drilling fluid circulation time here wasonly used for estimating the wellbore temperature profilesin the annulus In the simulation we fixed the well depth at1960m outlet drilling fluid rates at 16 Lsdotsminus1 and the casingpressure at 18MPa respectively The outlet gas rates wereassumed at a very low level with 001m3sdotsminus1 to eliminatethe effect of gas compressibility induced by the differenttemperatures Some important parameters for drilling fluidcan be read in Table 1 In contrast with constant drilling fluiddensity in traditional model the simulated results of wellborepressure using new model are observed being slightly lessin the lower part of the wellbore indicated in Figure 18The results also show that the wellbore pressure profiles aredifferent for different circulation time especially in bottomhole We can explain this by inspecting the temperatureprofiles change in Figure 19 Table 3 reports the values of thethermophysical properties used in the wellbore temperaturecalculation Caused by the cooling effect the rate of wellboreheat transfer diminishes with increasing circulation timeConsequently the temperature in wellbore declines withcirculating and engenders eventually the changes of densityprofile in Figure 20 which determines the wellbore pressuredirectly Data of a water-based drilling fluid from Isambourget al [15] reproduced in Table 4 are used here to calculate thedrilling fluid density
The results of the example show that the methodologyproposed here can estimate the reservoir pore pressure and
0 1000 2000 3000 4000 50000
6
12
18
24
30
36
42
Pres
sure
(MPa
)
Well depth (m)Constant density
4800 4840 4880 4920 4960 5000400
402
404
406
408
410
Pres
sure
(MPa
)
Well depth (m)
24h240h1200 h
Figure 18 Wellbore pressure profiles simulated using traditionalmodel and new model for different circulation time
0 1000 2000 3000 4000 5000300
320
340
360
380
400
420
440
Tem
pera
ture
(K)
Well depth (m)24h240h
1200 h
Figure 19 Temperature profiles simulated using new wellbore flowmodel for different circulation time
the permeability in real time and the estimated resultsare able to match the actual data to an acceptable levelHowever owing to the complexity of the subject someessential facets are necessary to provide to improve the qualityof the reservoir analysis when performing estimation ofpermeability and reservoir pore pressure during underbal-anced drilling First and most important the reservoir porepressure testing procedure should be initiated immediatelyonce visible gas flow from the reservoir is detected by thereal-time data monitoring system which indicates that gasreservoir has been opened For the reason that the linearcorrelation between the inflow and pressure at bottom exists
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
Journal of Applied Mathematics 15
Table 3 The values of the thermophysical properties for the calculation of temperature profile
119879
119890119894119887ℎ
K119879
119890119894119908ℎ
K119892
119879
Ksdotmminus1119892
119888
kgsdotmsdotNminus1sdotsecminus2119869
msdotNsdotJminus1119908
kgsdotsminus1119896
119890
Wsdotmminus1sdotKminus1119862
119901
Jsdotkgminus1sdotKminus1ℎ
119888
Wsdotmminus2sdotKminus1119870
119888119890119898
Wsdotmminus1sdotKminus1
427 303 003 100 100 3982 144 167472 909 402
0 1000 2000 3000 4000 5000100
101
102
103
104
105
Well depth (m)24h240h
1200 h
Dril
ling
fluid
den
sity
(gmiddotcm
minus3)
Figure 20 Drilling fluid density profile simulated using newwellbore flow model for different circulation time
Table 4 Empirical constants used in the drilling fluid densitycalculation (from Isambourg et al [15])
120574
119901
sdot1010
Paminus1120574
119901119901
sdot1019
Paminus2120574
119879
sdot104Kminus1
120574
119879119879
sdot107Kminus2
120574
119901119879
sdot1013
Kminus1Paminus1
2977 minus2293 minus1957 minus16838 0686
only at the earliest hours of transient inflow it is hard toacquire accurate estimation of the pore pressure once the bestopportunity is missed Moreover it is important to maintainthe wellbore in underbalance conditions while the reservoiris being penetrated and the underbalance should be smalland relatively stable The fluids can flow into the wellborefrom reservoir and be circulated out from the bottom holeonly when the well is drilled underbalance This is thefundamental premise of the reservoir characterization Thevariable underbalance introduces a further complication inthe reservoir analysis and produces less accurate estimatedresults of the permeability Thus the underbalance should bekept relatively stable by changing gas drilling fluid injectionrates or regulating the choke valve For better estimation ofthe permeability and well control low underbalance is alsoneeded In addition keeping constant and low penetrationrates is a benefit when performing reservoir characterizationduring underbalanced drilling For drilling operation thepenetration rates are relatively easy to control by regulatingartificially bit-weight in real time
7 Conclusion
In this study a methodology for estimating reservoir charac-terization during underbalanced drilling of horizontal wellshas been presented The main reservoir characterizationconsidered here is the reservoir pore pressure and per-meability profiles The methodology is established using amultiphase wellbore flowmodel merged with a transient wellinflux model of a horizontal well on the basis of the real-time data monitoring system for aerated drilling and liquid-based underbalanced drilling The methodology is appliedto estimate reservoir pore pressure and permeability Animportant aspect of themethodology presented is that we usean improved method to identify the reservoir pore pressurebased on the Kneisslrsquos methodology using a different testingprocedure
This methodology has been applied in approximately10 wells in China The estimated reservoir pore pressureand permeability are compared with the actual values fromwell test data and show a good agreement Owing to theintroduction of the models simulating the drilling fluiddensity behavior and wellbore heat transfer the multiphasewellbore flow model can be used to estimate the wellborebehavior more accurately which is very critical for reservoircharacterization during aerated underbalanced drilling
Appendices
A Closure Relationships of the TransientWellbore Flow Model
A1 Drag Forces In this paper the drag force acting on agas particle under steady state conditions can be expressedas follows
119865
119889119892=
3
8
120572
119892120588
119897119862
119889119892
(119906
119892minus 119906
119897)
1003816
1003816
1003816
1003816
1003816
119906
119892minus 119906
119897
1003816
1003816
1003816
1003816
1003816
119877
119901119892
(A1)
where 119862
119889119892is the drag coefficient given by Ishii and Mishima
[35] as the following expressionsFor the bubbly flow
119862
119889119892=
4119877
119901119892
3
radic
119892 (120588
119892minus 120588
119897)
120590
119904
[
[
1 + 1767[119891 (120572
119892)]
67
1867119891(120572
119892)
]
]
2
119891 (120572
119892) = (1 minus 120572
119892)
15
(A2)
where 119877
119901119892is the gas particle ratio and 120590
119904is the gas-liquid
interfacial tension given by Park et al [31]
120590
119904= minus03120588
119897(119906
119892minus 119906
119897)
2
(A3)
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
16 Journal of Applied Mathematics
According to the work of Lahey [36] the bubble radius119877
119901119892 is given by
119877
119901119892= [(
2
32
)(
120572
119892119881
120587
)]
13
(A4)
where 119881 is the total volume of every numerical nodeFor the slug flow
119862
119889119892= 98(1 minus 120572
119892)
3
(A5)
In this paper the flow patterns are confirmed using theflow pattern transition criteria from the work of Barnea [37]
A2 Virtual Mass Force The virtual mass force expresses themomentum exchange caused by relatively acceleratedmotion According to Lahey [36] the most common virtualmass force terms for gas phase can be expressed as
119865V119898 = 120572
119892120588
119897119862V119898 (
120597119906
119892
120597119905
minus
120597119906
119908
120597119905
+ 119906
119892
120597119906
119892
120597119911
minus 119906
119897
120597119906
119897
120597119911
) (A6)
where 119862V119898 denotes the virtual mass coefficient of gas phasegiven by Ishii and Mishima [35]
for the bubbly flow
119862V119898 =
1
2
120572
119892
1 + 2120572
119892
1 minus 120572
119892
(A7)
for the slug flow
119862V119898 = 5120572
119892[066 + 034 (
1 minus 119889
119905119887119871
119905119887
1 minus 119889
1199051198873119871
119905119887
)] (A8)
where 119889
119905119887and 119871
119905119887are respectively the long bubble diameter
and length of the bubble Taylor shown in Figure 21 Twoparameters can be calculated according thework ofKaya [38]
A3 Wall Shear Force In the present paper the wall shearforces in both bubbly flow and slug flow are discussed Forthe bubbly flow thewall shear force for gas phase is neglectedand the liquid wall shear stress is presented byWongwised etal [39] as follows
Γ
119897119908=
0046
2
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A9)
Then the liquid wall shear force can be given by
119865
119908119897=
Γ
119897119908119878
119897
119860
=
0046119878
119897
2119860
120588
119897119906
119897
1003816
1003816
1003816
1003816
119906
119897
1003816
1003816
1003816
1003816
(
119906
119897119889
120592
119897
)
minus02
(A10)
where119860 is the cross sectional area of the pipe 119878119897is the liquid-
wall wetted perimeter and 119889 is the diameter of the pipeFor the slug flow the effect of gas wall shear is no longer
neglected According to the work of Cazarez-Candia et al
u tbuuuuuuuuuuuuuuuu tttttttttttttttbbbbbbbbbbbbbbbbbb
Lsu
Ltb Lls
120591iultb ulls
Sl
Sl
Sg
Si
Sltb
Al
Al
Ag
120591gw
Figure 21 A schematic of key geometrical parameters in horizontalslug flow
[40] the wall shear forces for gas and liquid phase are cal-culated respectively as
119865
119908119892=
Γ
119892119908119878
119892120595
119897
4119860
119892
+
Γ
119892119894119878
119894
4119860
119892
119871
119905119887
119871
119904119906
119865
119908119897=
Γ
119897119908
4119871
119904119906
(
119878
119897119871
119897119904
119860
119897
+
119878
119897119905119887119871
119905119887
119860
119897119905119887
) +
Γ
119897119894119878
119894
4119860
119897
119871
119905119887
119871
119904119906
(A11)
where 119860 is the area 119878 is the perimeter and Γ is the shearstress Parameters 119871
119897119904 119871119904119906
are slug and slug unit lengthsrespectively The parameter 120595
1is used to modify the model
according to the deviation angle The subscripts 119892 119897 119894 and119908 denote gas liquid interface and wall respectively In thesame way the above geometrical parameters according to theregion in Figure 21 can be calculated using the means in theKayarsquos paper [38]
Shear stresses for angles from 0
∘ to 45∘ are given by Issaand Kempf [41]
Γ
119892119908=
119891
119892120588
119892119906
2
119892
2
Γ
119897119908=
119891
119897120588
119897119906
2
1
2
Γ
119897119894=
119891
119894120588
119892(119906
119892minus 119906
119897)
2
2
(A12)
where 119891 is friction factor can be given by
119891
119892=
16
Re119892
for Re119892le 2300
0046Re119892
minus02 for Re119892gt 2300
119891
119897=
24
Re119897
for Re119897le 2300
00262(120572
119897Re119897)
minus0139 for Re119897gt 2300
119891
119894=
16
Re119892
for Re119894le 2300
0046Re119894
minus02 for Re119894gt 2300
(A13)
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
Journal of Applied Mathematics 17
Gas liquid and interfacial Reynolds numbers are givenrespectively by
Re119897=
119889
119897119906
119897120588
119897
120583
119897
Re119892=
119889
119892119906
119892120588
119892
120583
119892
Re119894=
119889
119892(119906
119892minus 119906
119897) 120588
119892
120583
119892
(A14)
where 119889
119897 119889
119892are the liquid and gas hydraulic diameter
respectively given as follows
119889
119897=
4119860
119897
119878
119897
119889
119892=
4119860
119892
119878
119892+ 119878
119894
(A15)
For deviation angle over 45∘ the liquid wall shear stress isgiven by
Γ
119897119908=
119891
119897120588
119897119906
1
2
2119889
119897
120587119889 (A16)
where the friction factor is given by the followingfor laminar flow
119891
119897=
16
Re119897
(A17)
for turbulent flow
119891
119897= 0079Re
119897
minus025
(A18)
where
Re119897=
119889119906
119897120588
119897
120583
119897
(A19)
B Parameters of (7)The inverse relaxation distance 120585 is defined by
120585 =
119862
119901119908
2120587
(
119896
119890+ 119903
119905119900119880
119905119900119879
119863
119903
119905119900119880
119905119900119896
119890
) (B1)
where 119908 is total mass flow rate 119903
119905119900is outside radius of
drill string 119896119890is formation conductivity 119880
119905119900is overall heat
transfer coefficient and119879
119863is dimensionless temperatureThe
expression for 119880119905119900can be obtained from
119880
119905119900= [
1
ℎ
119888
+
119903
119905119900ln (119903
119908119887119903
119888119900)
119896
119888119890119898
] (B2)
where ℎ
119888is convective heat transfer coefficient for annulus
fluid 119903119908119887
is outside radius of wellbore 119903119888119900is outside radius
of wellbore and 119896
119888119890119898is cement conductivity
The value of dimensionless temperature can be obtainedusing the following algebraic approximation presented byHasan and Kabir [42]
119879
119863=
(11281radic119905
119863) times (1 minus 03radic119905
119863)
for 10
minus10
le 119905
119863le 15
(04063 + 05 ln 119905
119863) times (1 +
06
119905
119863
)
for 119905
119863gt 15
(B3)
where 119905119863is dimensionless time
The undisturbed formation temperature 119879119890119894 is generally
assumed to vary linearly with depth given as follows
119879
119890119894= 119879
119890119894119887ℎminus 119892
119879119911 (B4)
where 119879
119890119894119887ℎis undisturbed formation temperature at the
bottom hole which can be easily obtained by invoking theundisturbed formation temperature at the wellhead 119879
119890119894119908ℎ
In this work we use the empirical expression developedby Sagar et al [43] to estimate the value of 120593 as follows
120593 =minus 0002978 + 1006 times 10
minus6
119901
119908ℎ
+ 1906 times 10
minus4
119908 minus 1047 times 10
minus6
119865
119892119897
+ 3229 times 10
minus5
119860119875119868 + 0004009120574
119892minus 03551119892
119879
(B5)
where 119865
119892119897is the ratio of gas and liquid and 120574
119892is gas specific
gravity
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
The authors are grateful for the support of the NationalNatural Science Foundation of China (no 51104124 no51204140 and Grant no 51134004) Major state science andtechnology special project of China (no 2011ZX05021-003)and PhD Programs Foundation of Ministry of Education ofChina (Grant no 20125121110001)
References
[1] S P Smith G A Gregory N Munro and M Muqeem ldquoAppli-cation ofmultiphase flowmethods to horizontal underbalanceddrillingrdquo Journal of Canadian Petroleum Technology vol 39 no10 pp 52ndash60 2000
[2] K A Fattah S M El-Katatney and A A Dahab ldquoPotentialimplementation of underbalanced drilling technique in Egyp-tian oil fieldsrdquo Journal of King Saud UniversitymdashEngineeringSciences vol 23 pp 49ndash66 2011
[3] E H Vefring G Nygaard K K Fjelde R J LorentzenG Naeligvdal and A Merlo ldquoReservoir characterization duringunderbalanced drilling methodology accuracy and necessarydatardquo in Proceedings of the SPEAnnual Technical Conference andExhibition San Antonio Tex USA September-October 2002Paper SPE 77530
[4] E H Vefring G Nygaard R J Lorentzen G Nœvdal andK KFjelde ldquoReservoir characterization during underbalanced dril-ling (UBD) methodology and active testsrdquo SPE Journal vol 11no 2 pp 181ndash192 2006
[5] C B Kardolus and C P J W van Kruijsdijk ldquoFormation testingwhile underbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 521ndash528 San AntonioTex USA October 1997
[6] C P J W van Kruijsdijk and R J W Cox ldquoTesting whileunderbalanced drilling horizontal well permeability profilesrdquo
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
18 Journal of Applied Mathematics
in Proceedings of the SPE European Formation Damage Confer-ence Paper SPE 54717 The Hague The Netherlands May-June1999
[7] L Larsen and F Nilsen ldquoInflow predictions and testing whileunderbalanced drillingrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition Houston Tex USA October1999 Paper SPE56684
[8] F Azar-Nejad ldquoFormation evaluation while underbalanced dri-lling of horizontal wells with coiled tubing technologyrdquo inProceedings of the CSPG and Petroleum Society Joint ConventionDigging Deeper Finding a Better Bottom Line Paper SPE99-53Alberta Canada June 1999
[9] J L Hunt and S Rester ldquoReservoir characterization duringunderbalanced drilling a new modelrdquo in Proceedings of theSPECERI Gas Technology Symposium Paper SPE 59743 Cal-gary Canada April 2000
[10] J L Hunt and S Rester ldquoMultilayer reservoir model enablesmore complete reservoir characterization during underbal-anced drillingrdquo in Proceedings of the SPESPE UnderbalancedTechnical Conference and Exhibition pp 25ndash26 Houston TexUSA 2003 Paper SPE 81638
[11] D Biswas P V Suryanarayana P J Frink and S RahmanldquoAn improved model to predict reservoir characteristics duringunderbalanced drillingrdquo in Proceedings of the SPE AnnualTechnical Conference and Exhibition pp 1111ndash1121 Denver ColoUSA October 2003 Paper SPE 84176
[12] W Kneissl ldquoReservoir characterization whilst underbalanceddrillingrdquo in Proceedings of the SPEIADC Drilling ConferenceAmsterdamTheNetherlands February 2001 Paper SPEIADC67690
[13] W Kneissl and Y Kuhn de Chizelle ldquoA method of determiningproperties relating to an underbalanced wellrdquo Patent Applica-tion 00243311
[14] G Stewart S Lakshminarayanan J Villatoro and S BoutalbildquoVariable rate UBD production data facilitates reservoir char-acterizationrdquo in Proceedings of the SPEIADCManaged PressureDrilling and Underbalanced Operations Conference and Exhibi-tion pp 32ndash43 Kuala Lumpur Malaysia February 2010
[15] P Isambourg B T Anfinsen and C Marken ldquoVolumetricbehavior of drilling muds at high pressure and high tempera-turerdquo in Proceedings of the European Petroleum Conference pp157ndash165 Milan Italy October 1996
[16] G Aithoff A A Arian A B Kavaipatti G L Varsamis andL T Wisniewski ldquoMWD ultrasonic caliper advanced detectiontechniquesrdquo in Proceedings of the the SPWLA 39th AnnualLogging Symposium May 1998
[17] H Li G Li Y Meng G Shu K Zhu and X Xu ldquoAttenuationlaw of MWD pulses in aerated drillingrdquo Petroleum Explorationand Development vol 39 no 2 pp 250ndash255 2012
[18] L A Carlsen GNygaard andR Time ldquoUtilizing instrumentedstand pipe formonitoring drilling fluid dynamics for improvingautomated drilling operationsrdquo in Proceedings of the 1st IFACWorkshop on Automatic Control of Offshore Oil and Gas Pro-duction (ACOOG rsquo12) pp 217ndash222 Trondheim Norway June2012
[19] A D Spalding and D Middleton ldquoOptimum reception in animpulsive interference environmentmdashpart II incoherent recep-tionrdquo IEEE Transactions on Communications vol 25 no 9 pp924ndash934 1977
[20] R T Lahey Jr andDADrew ldquoThe three-dimensional time andvolume averaged conservation equations of two-phase flowrdquoAdvances in Nuclear Science and Technology vol 20 no 1 pp1ndash69 1989
[21] A R Hasan and C S Kabir ldquoAspects of wellbore heat transferduring two-phase flowrdquo SPE Production amp Facilities vol 9 no3 pp 211ndash216 1994
[22] I N Alves F J S Alhanati andO Shoham ldquoAunifiedmodel forpredicting flowing temperature distribution in wellbores andpipelinesrdquo SPE Production Engineering vol 7 no 4 pp 363ndash3671992
[23] E Karstad and B S Aadnoy ldquoDensity behavior of drilling fluidsduring high pressure high temperature drilling operationsrdquo inProceedings of the IADCSPE Asia Pacific Drilling TechnologyPaper SPE 47806 Jakarta Indonesia September 1998
[24] H Cho S N Shah and S O Osisanya ldquoA three-segmenthydraulic model for cuttings transport in coiled tubing hori-zontal and deviated drillingrdquo Journal of Canadian PetroleumTechnology vol 41 no 6 pp 32ndash39 2002
[25] J Li and S Walker ldquoSensitivity analysis of hole cleaning para-meters in directional wellsrdquo SPE Journal vol 6 no 4 pp 356ndash363 2001
[26] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores Itransport equationsrdquo Petroleum Science and Technology vol 29no 13 pp 1366ndash1376 2011
[27] G Espinosa-Paredes and O Cazarez-Candia ldquoTwo-regionaverage model for cuttings transport in horizontal wellbores IIinterregion conditionsrdquo Petroleum Science and Technology vol29 no 13 pp 1377ndash1386 2011
[28] L Zhou R M Ahmed S Z Miska N E Takach M Yu andM B Pickell ldquoExperimental study and modeling of cuttingstransport with aerated mud in horizontal wellbore at simulateddownhole conditionsrdquo in Proceedings of the SPE Annual Tech-nical Conference and Exhibition pp 1051ndash1062 Houston TexUSA September 2004 Paper SPE 90038
[29] R J Avila E J Pereira S Z Miska and N E Takach ldquoCor-relations and analysis of cuttings transport with aerated fluidsin deviated wellsrdquo SPE Drilling and Completion vol 23 no 2pp 132ndash141 2008
[30] L Zhou ldquoHole cleaning during underbalanced drilling inhorizontal and inclined wellborerdquo SPE Drilling and Completionvol 23 no 3 pp 267ndash273 2008
[31] J W Park D A Drew and R T Lahey Jr ldquoThe analysisof void wave propagation in adiabatic monodispersed bubblytwo-phase flows using an ensemble-averaged two-fluid modelrdquoInternational Journal ofMultiphase Flow vol 24 no 7 pp 1205ndash1244 1998
[32] N Petalas and K Aziz ldquoA mechanistic model for multiphaseflow in pipesrdquo Journal of Canadian Petroleum Technology vol39 no 6 13 pages 2000
[33] A C V M Lage Two-phase flow models and experiments forlow-head and underbalanced drilling [PhD thesis] StavangerUniversity College Stavanger Norway 2000
[34] C P J W van Kruijsdijk ldquoSemianalytical modeling of pressuretransient in fractured reservoirsrdquo in Proceedings of the SPEAnnual Technical Conference and Exhibition Houston TexUSA October 1988 Paper SPE 18169
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
Journal of Applied Mathematics 19
[35] M Ishii and K Mishima ldquoTwo-fluid model and hydrodynamicconstitutive relationsrdquo Nuclear Engineering and Design vol 82no 2-3 pp 107ndash126 1984
[36] R T Lahey Boiling Heat Transfer Modern Developments andAdvances Elsevier Amsterdam The Netherlands 1992
[37] D Barnea ldquoA unified model for predicting flow-pattern tran-sitions for the whole range of pipe inclinationsrdquo InternationalJournal of Multiphase Flow vol 13 no 1 pp 1ndash12 1987
[38] A S Kaya Comprehensive mechanistic modeling of two-phaseflow in deviated wells [MS thesis] The University of TulsaTulsa Okla USA 1998
[39] S Wongwises A Pornsee and E Siroratsakul ldquoGas-wall shearstress distribution in horizontal stratified two-phase flowrdquoInternational Communications in Heat and Mass Transfer vol26 no 6 pp 849ndash860 1999
[40] O Cazarez-Candia O C Benıtez-Centeno and G Espinosa-Paredes ldquoTwo-fluid model for transient analysis of slug flow inoil wellsrdquo International Journal of Heat and Fluid Flow vol 32no 3 pp 762ndash770 2011
[41] R I Issa and M H W Kempf ldquoSimulation of slug flowin horizontal and nearly horizontal pipes with the two-fluidmodelrdquo International Journal of Multiphase Flow vol 29 no 1pp 69ndash95 2003
[42] A R Hasan and C S Kabir ldquoHeat transfer during two-phase flow in wellboresmdashpart I Formation temperaturerdquo inProceedings of the the SPE Annual Technical Conference andExhibition vol 22866 Dallas Tex USA 1991
[43] R Sagar D R Doty and Z Schmidt ldquoPredicting temperatureprofiles in a flowing wellrdquo SPE Production Engineering vol 6no 4 pp 441ndash448 1991
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of
Submit your manuscripts athttpwwwhindawicom
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical Problems in Engineering
Hindawi Publishing Corporationhttpwwwhindawicom
Differential EquationsInternational Journal of
Volume 2014
Applied MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Probability and StatisticsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Mathematical PhysicsAdvances in
Complex AnalysisJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
OptimizationJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
CombinatoricsHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Operations ResearchAdvances in
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Function Spaces
Abstract and Applied AnalysisHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of Mathematics and Mathematical Sciences
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Algebra
Discrete Dynamics in Nature and Society
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Decision SciencesAdvances in
Discrete MathematicsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom
Volume 2014 Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Stochastic AnalysisInternational Journal of