xu effects of a gpc-pid control strategy with
DESCRIPTION
GPC-PIDTRANSCRIPT
www.elsevier.com/locate/enconman
Energy Conversion and Management 47 (2006) 132–145
Effects of a GPC-PID control strategy withhierarchical structure for a cooling coil unit
Min Xu a, Shaoyuan Li a,*, Wen-jian Cai b, Lu Lu b
a Department of Automation, Institute of Automation, Shanghai Jiao Tong University, 1954 Hua-Shan Rd.,
Shanghai 200030, PR Chinab School of Electrical and Electronic Engineering, Nanyang Technological University, Singapore 639798, Singapore
Received 19 February 2004; received in revised form 29 September 2004; accepted 30 March 2005
Available online 23 May 2005
Abstract
This paper presents a GPC-PID control strategy for a cooling-coil unit in heating, ventilation and air
conditioning systems. By analysis of the cooling towers and chillers, different models in the occupied period
are considered in each operating condition. Because of the complication of components, well tuned PID
controllers are unsatisfied, and the results are poor over a wide range of operation conditions. To solve this
problem, a GPC-PID controller with hierarchical structure is proposed based on minimizing the general-
ized predictive control criterion to tune conventional PID controller parameters. Simulation and experi-
ments show that the proposed controller is able to deal with a wide range of operating conditions andto achieve better performance than conventional methods.
� 2005 Elsevier Ltd. All rights reserved.
Keywords: Heating, ventilation and air-conditioning systems; Generalized predictive control; A cooling coil unit; PID
0196-8904/$ - see front matter � 2005 Elsevier Ltd. All rights reserved.
doi:10.1016/j.enconman.2005.03.012
* Corresponding author. Tel./fax: +862162932114.
E-mail address: [email protected] (S. Li).
Nomenclature
Symbols
Tcwi chilled water inlet temperatureTcwo chilled water outlet temperatureTai dry bulb temperature in on-coil stateTao dry bulb temperature in off-coil stateTaiwb wet bulb temperature in on-coil stateTaowb wet bulb temperature in off-coil stateFa air flow of cooling coilFcw chilled water flow rateQ real cooling load provided by all chillersccw chilled water specific heatca air specific heatc1,c2,e parameters in cooling coil modelf non-linear time varying functionKP proportional gainKi integral parameterKd derivative parameterN0 minimum predictive horizonN1 maximum predictive horizonNu control horizony(k + j) system output at time k + j
yðk þ jÞ system predictive output at time k + je(k) error at time kw0,w1,w2 proposed controller parametersJ performance indexr(k) system output at time k
G,E,F,H two Diophantine equation parameter
AbbreviationsAHU air handling unitPID proportional integral derivativeGPC generalized predictive controlFOPDT first-order plus dead timeFIR finite impulse responseCARIMA controlled autoregressive and integrated moving average modelVSD variable speed drivesCCU cooling coils unitHVAC heating, ventilation and air-condition
M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145 133
134 M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145
1. Introduction
In most large air conditioned buildings, air handling units (AHUs) account for a significantportion of the total building energy consumption and have a major effect on comfort conditionsand maintenance costs. Besides, because of the practical characteristics of AHUs and the con-straints imposed by non-ideal actuators, AHUs can be considered as highly non-linear systems[1]. Therefore, the control problem for AHUs is both difficult and important. Generally, AHUsadopt the standard proportional integral derivative (PID) control method to maintain the supplyair temperature at the set point value by changing the chilled water flow. This control method hasa simple structure, a few parameters and robustness to disturbance. This method is favorable onthe assumption that the system model parameters vary in a narrow range [2]. However, a control-ler for an AHU should be designed to cope with a wide range of operating conditions because ofthe multiple time varying processes taking place in the system. The use of fixed gain PID control-lers is not likely to give satisfactory performance, even with a well tuned PID controller, whenapplied to another system with different model parameters and results in poor response. There-fore, an adaptive controller, which can solve the AHU problem and obtain better performanceover a large range of operating condition, is highly desirable.
Over decades, numerous studies related to advanced algorithms for AHU systems appear in theliterature [3–5]. Generalized predictive control (GPC), which intends to solve an optimizationproblem subject to system constraints for a finite future at the current time and to implementthe first optimal control input as the current control input, is another self tuning techniqueattempted by many researchers [6].
In this paper, we are interested in developing a hierarchical structure control scheme forincorporating GPC into the PID controller. The reasons lie in:
• Once advanced algorithms (such as GPC) are adopted, the existing equipment, especially hard-ware parts, has to be upgraded at a large cost.
• The engineering level and the complicated algorithm will prohibit the implementation of theadvanced control method.
• The advanced tuning methods usually lack explicit specifications and the plant operators areunfamiliar with the parameters tuning.
The proposed hierarchical structure control strategy consists of two levels, a basic level and anoptimization level. The basic level is a conventional PID controller, which is not likely to give sat-isfactory performance as operating conditions change. Through predicting system output andminimizing the GPC criterion in the optimization level, the gain of the PID controller is a vari-able, changing with time, to cater for the changing system and the environmental uncertainties.As a matter of fact, the closed loop performance equals that of the standard GPC, while the prac-tical controller still remains a PID structure to plant personnel. Hence, it is not necessary thatthey grasp the advanced algorithm, and the system performance can be improved with only aminor cost. Simulations and experiments are conducted for a cooling coil unit in an AHU sys-tem, and the results show performance improvement and a significant reduction of the operatingcost.
M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145 135
2. Air handing unit and control
2.1. Main components of the system
A schematic diagram of an AHU is shown in Fig. 1. It consists of coils, air dampers, fans,pumps, filters and valves.
Fresh air from outdoors enters the AHU through the outdoor air damper and may be mixedwith air passing through the recirculation air dampers depending on the mixing box damper set-tings. The temperatures and flow rates of the outdoors and recirculation air streams determine theconditions at the exit of the mixed air plenum. Air, which is exiting the mixed air plenum, passesthrough heating or cooling coils. At most, only one of the two coils will be active at any given timeif implemented properly and there are no valve leaks or other faults in the system. Here, we onlyconsider a cooling coil. After being conditioned in the coils, the air is distributed to the zonesthrough the supply air ductwork. The supply air temperature is measured downstream of the sup-ply fan. Return air is drawn from the conditioned zones by the return fan and is exhausted orrecirculated, depending once again on the position of the mixing box dampers. The return airtemperature is measured downstream of the return fan.
Control parameters of an AHU system are the temperature and flow rate of the conditioned air.To build a closed loop control system, the parameters to be measured are the following: dry bulbtemperatures, wet bulb temperature and the air flow of the cooling coil.
2.2. Plant modeling
Because thermal loads for the zones can vary markedly, it is common for a cooling coil unit tobe controlled to maintain the supply air temperature Tao at a set point value that is sufficiently low
Damper Motor
Outer Air Damper
Exhaust Fan
SupplyFan
Recirculation Air Damper
ReturnFan From Zones
To Zones
Mixed Air Plenum
Return Air Plenum
Filter
Supply Air
Temperature & Flow SensorT& F
T& FFa Fa
Cooling
Coil
FilteraiT aiwbT aoT aowbT
T&F Valve
Chilled water
cwT cwF
Exhausted Air
Fig. 1. Schematic diagram of conventional AHU control system.
136 M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145
to satisfy the zone with the largest cooling load at any given time. The output Tao can be describedas follows and is influenced by Fcw, Fa, Tai and Tcwi:
T ao ¼ f ðF cw; F a; T ai; T cwiÞ ð1Þ
In the steady-state, Eq. (1) can be explicitly expressed by [7]Q ¼ c1F ea
1 þ c2F a
F cw
� �e ðT ai � T cwiÞ ð2Þ
and
Q ¼ ccwF cwðT cwo � T cwiÞ ¼ caF aðT ai � T aoÞ ð3Þ
Combining Eqs. (2) and (3), Tao can be written as followsT ao ¼ T ai �ðc1=caÞF e�1
a F ecw
F cw þ c2F ea
ðT ai � T cwiÞ
These system variables change with the air and water flow rate. If the air flow rate or chilled waterflow rate is high, the time constant and time delay will be smaller, and vice versa.
2.3. Basic level control strategy
In a cooling coil unit, plant engineers usually adopt the conventional velocity PID controller inthe basic level:
DuðkÞ ¼ ½Kp þ K i þ Kd�eðkÞ þ ½�Kp � 2Kd�eðk � 1Þ þ Kdeðk � 2Þ¼ w0eðkÞ þ w1eðk � 1Þ þ w2eðk � 2Þ
ð4Þ
where w0 = Kp + Ki + Kd, w1 = �Kp � 2Kd and w3 = Kd.As system exhibits nonlinear behavior, the resulting system performance with conventional PID
controller is reduced, especially when the controllers operates over a wide range of operating con-ditions. One solution to alleviate the problem is continually to retune the basic level controllerparameters over a wide range operating conditions. The other is to design advanced controllerto enable a wider operating conditions. Because of constraints on time availability of plant per-sonnel and running cost of the plant, the former solution is commonly adopted. Therefore, wedesign the advanced predictive control algorithm incorporating basic level PID controller, toretune the basic level controller parameters through receding horizon window on the minimiza-tion of GPC criterion.
Over a large range of operating conditions, the controller parameters vary with time, so thecontroller can be expressed in the following format:
DuðkÞ ¼ w0ðkÞeðkÞ þ w1ðkÞeðk � 1Þ þ w2ðkÞeðk � 2Þ ¼X2
i¼0
wiðkÞeðk � iÞ ¼ WTðkÞeðkÞ ð5Þ
where
WTðkÞ ¼ w0ðkÞ w1ðkÞ w2ðkÞ½ � eðkÞ ¼ eðkÞ eðk � 1Þ eðk � 2Þ½ �T
M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145 137
3. A GPC-PID strategy with hierarchical structure
3.1. Optimization level control strategy
The drawback of the conventional PID controller is that it has three degrees of freedom in tun-ing, which is difficult for plant engineers to tune the parameters to meet different specifications.Hence, in this paper, a GPC-PID control strategy with hierarchical structure is proposed. A basiclevel and an optimization level are consisted of the hierarchical control structure. The basic levelcontroller parameters are retuned via the optimization level based on the identification modelthrough minimizing the performance index. Since the identification model and criterion is thesame with that of the standard GPC control algorithm, better performance than conventionalPID controller is obtained in the hierarchical structure.
The cooling coil unit to be controlled can be described as a CARIMA model, and j-step systemoutput can be derived by using two Diophantine equations [8]:
yðk þ j jkÞ ¼ GjDuðk þ j� 1Þ þ HjD�uðk � 1Þ þ F j�yðkÞ
where Gj and Hj are polynomials with respect to q�1 of degree j � 1 and maxðnEB � jþ 1; n� 1Þ,respectively. D�uðk � 1Þ ¼ Duðk � 1Þ=C and �yðkÞ ¼ yðkÞ=C, where C is assumed as the minimumphase and is supposed to be C(z�1) = 1.Substituting Eq. (5) into the above equation yields
yðk þ j jkÞ ¼ Gj
X2
i¼0
wiðkÞeðk � iÞ !
þ HjDuðk � 1Þ þ F jyðkÞ
Therefore, the optimal control variable can be obtained through the GPC criterion.When model and environment uncertainty is presented, the prior well tuned parameters are no
longer suitable, the optimization level starts to work and finds the optimal controller parameters{w0(k),w1(k),w2(k)} via a receding horizon optimization method based on a multistage costfunction,
J ¼ EXN1
j¼N0
½yðk þ j jkÞ � rðk þ jÞ�2 þXNu
j¼1
kðjÞ½Duðk þ j� 1Þ�2( )
ð6Þ
Substituting Eq. (5) into Eq. (6), the cost function becomes:
J ¼ EXN1
j¼N0
½eðk;W Þ�2 þXNu
j¼1
kðjÞ½W ðkÞeðkÞ�2( )
Suppose W*(k � 1) is the optimal parameter vector for minimization of J(k � 1,W) at the timek � 1.
To achieve an optimal control variable at time interval k, a second-order Taylor expansion ofJ(k,W) over W*(k � 1) is given by
138 M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145
Jðk;W Þ Jðk;W ðk � 1ÞÞ þ dJðk;W ÞdW
����W ðk�1Þ
� ðW � W ðk � 1ÞÞ þ 1
2ðW �W ðk � 1ÞÞT
� d2Jðk;W ÞdW 2
����W ðk�1Þ
� ðW �W ðk � 1ÞÞ þ Oð=W � W ðK � 1Þ=3Þ ð7Þ
where O(W) is the higher order expansion terms. By minimizing Eq. (7) with respect to W, theresult is shown as follows:
W ðkÞ ¼ W ðk � 1Þ þ P ðkÞ eðk;W ðk � 1ÞÞ � Sðk;W ðk � 1ÞÞ � kW ðk � 1ÞeðkÞeTðkÞ½ �
PðkÞ ¼ QðkÞ � kQðkÞeðkÞeTðkÞQðkÞ½eTðkÞPðkÞeðkÞ þ 1�
QðkÞ ¼ Pðk � 1Þ � kP ðk � 1ÞSðkÞSTðkÞP ðk � 1Þ½STðkÞP ðk � 1ÞSðkÞ þ 1�
Sðk;W ðk � 1ÞÞ ¼ � deðk;W ÞdW
����W ðk�1Þ
8>>>>>>>>>>>><>>>>>>>>>>>>:
ð8Þ
In practice, the signal Du(k)given by W(k) at time k is computed and executed to the system, andat time k + 1, a new control action Du(k + 1) is recalculated with the estimated model and the cri-terion on a moving horizon window. Since the estimated model is a CARIMA form, the control-ler, through minimizing the criterion via receding horizon optimization, is equal to that ofgeneralized predictive control.
Under the condition k > 0, as the predictive horizon is larger than the amount of the controlhorizon, we can guarantee the closed loop asymptotical stability through adjusting the predictivehorizon and control horizon. Simultaneously, it is guaranteed that the maximum predictive hori-zon is larger than the upper of the time delay and the deterioration of performance will be small.
The GPC-PID control strategy with hierarchical structure is given as follows:
Step 1: Estimate the nominal CARIMA model to yieldG, H and F.Step 2: Set maximum and minimum predictive horizons and control horizon.Step 3: Initialize starting values as W*(0) = 0, P(0) = I.Step 4: Compute the W*(k) based on Eq. (8) through the predictive horizon.Step 4: Set the control law at the sample time k, as Du(k) = W*(k)e(k).Step 5: At the next sample timek + 1, go back to step 3 and obtain the next optimal control
value.
Thus, the optimal parameters are retuned at any sample time to obtain better performance thanthe conventional PID controller.
4. Simulation and experimental results
The experiment and simulation are also conducted on a typical HVAC system [9] (shown inFig. 2). There are five heat transfer loops: indoor air loop that includes fans, cooling coils, terminal
rooms & dampers
coil fans & ducts
cooling coils & valves
pumps &
pipes
evap
orat
ors
cond
ense
rs
compressorwater pumps
cooling towers
indoorair
chilledwater
condenser water
outdoor air
refrigerant
chillers
tower fans
outd
oor
envi
ronm
ent
outd
oor
envi
ronm
ent
Fig. 2. The plant of a typical HVAC system.
M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145 139
units, dampers and ducts; chilled water loop that includes pipes, pumps, cooling coils, chiller evap-orators and valves; refrigerant loop that includes evaporators, compressors, condensers andexpansion valves; condenser water loop that includes cooling towers, chiller condensers andpumps; outdoor air loop includes fans and cooling towers. All motors (fans, pumps and compres-sors) are equipped with variable speed drives (VSD) to control the motor speed.
We consider cooling coils units (CCU) with the dimensions of 25 cm · 25 cm · 8 cm for theAHU system whose schematic diagram is shown in Fig. 3. The system requires a differential pres-sure sensor across each cooling coil to monitor the chilled water flow rate as well as to estimate thecooling load of each coil. The sensors are also to control the opening positions of control valves toconstrain the chilled water flow. Another differential pressure sensor is mounted to monitor thepump head, which is used to control the VSD pump speed. Each coil also requires a tempera-ture sensor to measure the chilled water return temperature together with a common chilled watersupply temperature sensor to estimate the cooling load of each coil.
Each piping branch consists of a cooling coil and a two-way control valve. The two-way controlvalve is modulated to keep the off coil air temperature constant for the varying supply air volumein response to the varying cooling demand. The pump speed is modulated by a differential pres-sure sensor to keep the pressure differential of the farthest away branch (coil + valve) constant.The set point of a constant pressure differential is often chosen on the basis of the designedfull load condition. Sometimes, a safety factor is added to make sure that each coil has enoughpressure drop.
Chilled water pump
Chilled water in
Cooling coilcwiTcwF
Chilled water out
Air in Air out
cwoT
aF
aiT aiwbT
aF
aoT aowbT
Fig. 3. Schematic diagram of a cooling coil.
140 M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145
The measured signals for the experiment are the air and water flow rates, on coil air dry bulb/wet bulb temperatures and cooling coil inlet and outlet water temperatures. The experiment isconducted under the following conditions: the chilled water supply temperature is fixed; the cool-ing load variation is achieved through the air and water flow rates. The curve fitting results of themodel in Eq. (2) are c1 = 0.45, c2 = 0.70, e = 0.61. This is a non-linear model, and the model islinearized at three different operating condition.
Different controller parameters and system parameters at different operating condition is shownin Table 1. A result is shown in Fig. 4 based on the Table 1 controller parameters. At the stage 1,optimal PID controller parameters are selected [10] and a short rise time and no overshoot areobtained. At the stage 2, a large oscillation is obtained, since controller parameters cannot be se-lected again. Next stage, system is divergence for different operating condition. As can be seen inFig. 3, because conventional PID controller is chosen based on the stage 1 operating condition,system performance is unsatisfied for different operating condition. The same, we switch to theproposed controller in stage 3, better performance than conventional PID controller can beobtained (shown in Fig. 5). Fig. 6 shows the performance of the GPC-PID under a square waveset point change. It is clear that a better performance is achieved through the GPC-PID controlstrategy. Whereas it is difficult to apply one set of PID controller parameters to obtain good per-formance for the whole range of operating condition. Although tuning the controller at the pointof highest process gain is possibly to overcome system oscillation, it may result unsatisfied controlperformance under other stages of operating condition (seen in Fig. 7). To verify the robustness to
Table 1
Three level plant models with wide range (Figs. 3 and 4)
System parameters GPC-PID scheme Optimal PID parameter
a3 a2 a1 a0 b0 d N0 N1 Nu k KP Ki Kd
Stage 1 0 0 1 0.2 0.2 0 0 0 0 0 4 2.8 0.1
Stage 2 0 1 0.6 0.02 0.02 0 0 0 0 0
Stage 3 1 0.52 0.18 0.02 0.04 5 1 5 3 0.7
0 100 200 300 400 500 600 700 800 900 1000(s)
-1
0
1
2
3
syst
em o
utpu
t
Stage 1 Stage 2
Stage 3
Fig. 4. PID control scheme with optimal controller parameters.
0 100 200 300 400 500 600 700 800 900 1000(s)0
0.5
1
1.5
syst
em o
utpu
t
Stage 1 Stage 2 Stage 3
Fig. 5. GPC-PID control scheme for stage 3.
0 100 200 300 400 500 600(s)-0.5
0
0.5
1
1.5
syst
em o
utpu
t
stage 1 stage 2 stage 3
Fig. 6. System output with the proposed strategy for the whole operating condition.
0 100 200 300 400 500 600(s)
-1
0
1
2
syst
em o
utpu
t
stage 1 stage 2 stage 3
Fig. 7. System output with optimal PID controller.
M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145 141
142 M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145
the disturbance, a white noise with 0.1 dithers are introduced in the controlled loop. As can beseen in Fig. 8, a satisfied control performance with small oscillation is obtained.
Figs. 9–11 show the different responses of fixed well tuned parameters PID controller and GPC-PID control strategy in the case of a temperature set point change and chilled water flow ratefluctuation.
First, we let the off coil temperature stabilize at 18.7 �C, and then the set point goes up to19.5 �C with a stable flow rate for the chilled water at the time t = 250 s.
Second, we increase the air flow rate, which leads to an increase of the water flow rate. The tem-perature set point remains unchanged to the time t = 1500 s.
Third, we decrease the air flow rate, which leads to a decrease of the water flow rate. The tem-perature set point remains unchanged to the time t = 2200 s.
Based on the same operating condition, the fixed well tuned PID controller is designed in spiteof the disturbance of the air flow rate. From Figs. 10 and 11, the overshoot of the output is largerthan 0.7�, while the PID controller tuned via the receding horizon optimization is only up to 0.2�.
0 100 200 300 400 500 600(s)-0.5
0
0.5
1
1.5
syst
em o
utpu
t
stage 1 stage 2 stage 3
Fig. 8. System output with the proposed strategy in the presence of output disturbances.
Fig. 9. The air flow rate change.
Fig. 10. Conventional PID control method.
Fig. 11. The GPC-PID control strategy.
M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145 143
5. Conclusions
A novel receding horizon optimization algorithm based on the GPC criterion and CARIMAmodel, has been developed for an CCU system. Simulation and experiments show that the con-troller is able to reject the effects of both static and dynamic disturbances rapidly. The perfor-mance of the CCU system is improved compared with that of the conventional well tuned PIDcontroller. Without major change of hardware and software, the controller can self tune theparameters of the PID controller with one degree of freedom.
Acknowledgements
The authors would like to acknowledge the financial support of the National Science Founda-tion of China (Grant No. 60474051) and Development Program of Shanghai Science and Tech-nology Department under Grant 04DZ11008, and partly by the Specialized Research Fund forthe Doctoral Program of Higher Education of China under Grant 20020248028. The authorsare grateful to the anonymous reviewers for their valuable recommendations.
144 M. Xu et al. / Energy Conversion and Management 47 (2006) 132–145
Appendix A
The criterion given by Eq. (6) can be rewritten as
Jðk;W Þ ¼ ½rðk þ jÞ � yðk þ j jkÞ�2 þ k½W TðkÞeðkÞ�2 ð9Þ
Differentiating this expression twice with respect toWdJðk;W ÞdW
����W ðk�1Þ
¼ eðk;W ðk � 1ÞÞdeðk;W ÞdW
����W ðk�1Þ
þ kðW ðk � 1ÞÞTeðkÞeðkÞ ð10Þ
When k is large enough, the optimal W*(k) is very close to W*(k � 1), and then the followingapproximation is rational.
OðW ðkÞ � W ðK � 1ÞÞ ! 0
d2Jðk;W ÞdW 2
����W ðk�1Þ
d2Jðk;W ÞdW 2
����W ðkÞ
ð11Þ
Using Eqs. (10) and (11), the optimal vector W*(k) is written as
W ðkÞ ¼ W ðk � 1Þ þ RðkÞ�1½eðk;W ðk � 1ÞÞ Sðk;W ðk � 1ÞÞ � kW ðk � 1ÞeðkÞeTðkÞ�
whereRðkÞ ¼ d2Jðk;W ÞdW 2
����W ðkÞ
ð12Þ
Sðk;W ðk � 1ÞÞ ¼ � deðk;W ÞdW
����W ðk�1Þ
Applied the known lemma, we can conclude Eq. (9)
W ðkÞ ¼ W ðk � 1Þ þ P ðkÞ½eðk;W ðk � 1Þ Sðk;W ðk � 1ÞÞ � kW ðk � 1ÞeðkÞeT ðkÞ�
PðkÞ ¼ QðkÞ � kQðkÞeðkÞeT ðkÞQðkÞ½eT ðkÞPðkÞeðkÞ þ 1�
QðkÞ ¼ Pðk � 1Þ � kP ðk � 1ÞSðkÞST ðkÞP ðk � 1Þ½ST ðkÞP ðk � 1ÞSðkÞ þ 1�
Sðk;W ðk � 1ÞÞ ¼ � deðk;wÞdW
����W ðk�1Þ
8>>>>>>>>>><>>>>>>>>>>:
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