optimization of high voltage cable dimension in scania
TRANSCRIPT
IN DEGREE PROJECT ELECTRICAL ENGINEERING,SECOND CYCLE, 30 CREDITS
, STOCKHOLM SWEDEN 2019
Optimization of High Voltage Cable Dimension in Scania Electric Vehicleβs Systems
HERALDUS PANJI ARIKSON
KTH ROYAL INSTITUTE OF TECHNOLOGYSCHOOL OF ELECTRICAL ENGINEERING AND COMPUTER SCIENCE
Optimization of High Voltage Cable Dimension in Scania Electric Vehicleβs Systems
Author
Heraldus Panji Arikson <[email protected]>
KTH Royal Institute of Technology
Program
MSc Electric Power Engineering
Place and Date
KTH Royal Institute of Technology, Stockholm, Sweden
Scania Tekniskt Centrum, SΓΆdertΓ€lje, Sweden
September 2019
Examiner
Hans Edin
KTH Royal Institute of Technology
Supervisors
Fadi Hanna
Scania
Nathaniel Taylor
KTH Royal Institute of Technology
With the increasing demand for electrified vehicles, the demand for electrical
components, including cables, is rising too. Thus, it is important to develop a method to
optimize the cable sizing to ensure the cable is technically robust and economically efficient.
The aim of this project is to study and evaluate different cablesβ designs to find the optimum
dimension for βhigh voltageβ class (automotive voltage class B) cables in the electrical
vehicle system. Three important technical aspects in evaluating the optimum cross-section
area (CSA) are the ampacity of the cable, short-circuit withstand capability and voltage drop.
In this project, the ampacity of a cable placed in air is calculated by the analytical
method based on IEC 60287 and by a finite-element simulation. These results are verified
against direct measurements using a dc source and load. In DC calculation, the similarity of
all three methods is high, within 96%. The formation of the cable also affects the ampacity
of the cable. For DC currents, the vertical formation has a higher ampacity than the
horizontal formation, by almost 2%. For AC currents, the trefoil formation has a higher
ampacity than the horizontal and vertical formation, by around 6-9%.
Calculations of short circuit withstand capability and voltage drop were performed to
ensure cable performance. The larger CSA corresponds to both higher short circuit capability
and lower voltage drop. In a short circuit, a duration around 0.5 s is critical since there is a
significant difference between short circuit withstand capability before and after this.
Voltage drop calculation is performed to ensure that the combination of CSA and length
does not exceed 3% voltage drop at the load end side of the circuit. The Voltage drop is not
found to be an important factor to consider. Based on those three factors, the optimization
process is described with a flowchart.
EfterfrΓ₯gan pΓ₯ elfordon ΓΆkar, och dΓ€rmed ΓΆkar ocksΓ₯ efterfrΓ₯gan pΓ₯ den elektriska
komponenten. DΓ€rfΓΆr Γ€r det viktigt att utveckla en metod fΓΆr att optimera kabelstorleken sΓ₯
att kabeln Γ€r tekniskt robust och ekonomiskt effektiv. Syftet med detta projekt Γ€r att
studera och utvΓ€rdera olika kablarnas konstruktioner fΓΆr att hitta den optimala dimensionen
fΓΆr hΓΆgspΓ€nningsklass (spΓ€nningsklass B) i elfordonssystemet. Tre viktiga tekniska aspekter
vid utvΓ€rderingen av den optimala kabelstorleken Γ€r kabelns kapacitet,
kortslutningsfΓΆrmΓ₯ga och spΓ€nningsfall.
I detta projekt placeras kabeln i luften. Ampaciteten berΓ€knas med hjΓ€lp av en
analytisk metod baserad pΓ₯ IEC 60287 och en simulering med finita element metoden.
Dessa resultat verifieras mot direkta mΓ€tningar med hjΓ€lp av en likstrΓΆmskΓ€lla och elektrisk
belastning. FΓΆr DC-berΓ€kning Γ€r likheten fΓΆr alla tre metoderna mycket hΓΆg. Bildningen av
kabeln pΓ₯verkar ocksΓ₯ kabelns ampacitet. FΓΆr DC-strΓΆmmar har den vertikala formationen
en hΓΆgre ampacitet Γ€n den horisontella formationen fΓΆr nΓ€stan 2%. FΓΆr vΓ€xelstrΓΆmmar har
trefoilformationen en hΓΆgre ampacitet Γ€n den horisontella och vertikala formationen med
6-9 %.
KortslutningsfΓΆrmΓ₯gan och spΓ€nningsfallberΓ€kningen utfΓΆrdes fΓΆr att sΓ€kerstΓ€lla kabelprestanda. En stΓΆrre CSA innebΓ€r hΓΆgre kortslutningsfΓΆrmΓ₯ga och lΓ€gre spΓ€nningsfall. SpΓ€nningsfallberΓ€kning utfΓΆrs fΓΆr att begrΓ€nsa kabellΓ€ngden fΓΆr att sΓ€kerstΓ€lla ett maximalt 3% spΓ€nningsfall vid kretsens lastΓ€ndsida. SpΓ€nningsfallet Γ€r en viktig faktor att beakta. Med hjΓ€lp av dessa tre faktorer beskrivs optimeringsprocessen med ett flΓΆdesschema.
Contents ..................................................................................................................................2
......................................................................................................................3
List of Tables ...........................................................................................................................6
List of Figures ..........................................................................................................................7
Introduction ...............................................................................................................1
Study Literature Review .............................................................................................4
Cable Properties and Heat Sources ............................................................................8
Cable Components ............................................................................................................8
Heat Sources in the Cable ................................................................................................10
Conductor Losses (Wc) .............................................................................................10
Dielectric Losses (Wd)...............................................................................................12
Loss factor for sheath and screen (Ws) .....................................................................13
Thermal Resistance .........................................................................................................14
Thermal Resistance of the inner insulation (T1) ........................................................15
Thermal resistance between sheath and Armor (T2) ................................................15
Thermal Resistance of outer insulation (T3) .............................................................15
External Thermal Resistance (T4) .............................................................................15
Conductor Material .........................................................................................................16
Heat Transfer...................................................................................................................17
Ampacity, Short Circuit & Voltage Drop in the Cable ................................................18
Ampacity .........................................................................................................................18
Short Circuit Current ........................................................................................................19
Voltage Drop ...................................................................................................................20
Simulation Method and Experimental Setup ............................................................22
Simulation Set Up ............................................................................................................23
Experimental Set Up ........................................................................................................24
Result and Analysis ..................................................................................................27
Ampacity Calculation .......................................................................................................27
Losses Calculation .....................................................................................................27
AC Ampacity Result ...................................................................................................30
DC Ampacity Result...................................................................................................37
Conductor Material Comparison ...............................................................................44
Short Circuit Calculation ..................................................................................................46
Voltage Drop Calculation .................................................................................................49
Cable Optimization Process ......................................................................................52
Conclusion ...............................................................................................................54
Future Work.............................................................................................................56
Appendix ...................................................................................................................................57
Formula .................................................................................................................................57
Figure ....................................................................................................................................61
AC Ampacity ......................................................................................................................61
DC Ampacity ......................................................................................................................63
Voltage Drop .....................................................................................................................64
Matlab Code..........................................................................................................................66
Ampacity Calculation .........................................................................................................66
Short Circuit Calculation Code ...........................................................................................73
Voltage Drop Calculation Code ..........................................................................................74
Bibliography ..............................................................................................................................77
List of Tables
Table 1. Circuit Loading Multiplication Factors ............................................................................4
Table 2. Normalized Comparison of Copper and Aluminium Characteristic [17] ........................16
Table 3. Heat Dissipation Coefficient [14] ..................................................................................22
Table 4. Cable Section Material Properties ................................................................................23
Table 5. General Material Properties .........................................................................................27
Table 6. Loss Factor for Screen ..................................................................................................29
Table 7. Comparison of Temperature Development Calculation in AC Horizontal Formation.....31
Table 8. Comparison of Temperature Development Calculation in AC Vertical Formation .........33
Table 9. Comparison of Temperature Development Calculation in AC Trefoil Formation ...........34
Table 10. Comparison of Temperature Development Calculation in AC Multicore Cable ...........35
Table 11. AC Cable Ampacity .....................................................................................................37
Table 12. Comparison of Temperature Development Calculation for DC in Horizontal
Formation .................................................................................................................................39
Table 13. Comparison of Temperature Development Calculation for DC in Vertical Formation .41
Table 14. Comparison of Temperature Development Calculation for DC Multicore Cable .........42
Table 15. DC Cable Ampacity .....................................................................................................43
Table 16. Short Circuit Withstand Capability of a Cable .............................................................48
Table 17.Maximum Length of DC Application Cable ..................................................................50
List of Figures
Figure 1. Evolution of the global electric car stock from 2013 to 2017 [1]....................................1
Figure 2. Global EV stock in the New Policies and EV30@30 scenarios, 2017-30 [1] ....................2
Figure 3. Optimization Process for Cross Sections [8] ..................................................................6
Figure 4. Cable Layers for Single-core ..........................................................................................8
Figure 5. Two Core Cable Cross Sectional ....................................................................................9
Figure 6. Cable Heat Equivalent Circuit ......................................................................................10
Figure 7. Skin Effect in AC Conductor (b) compared to DC Conductor (a) ...................................11
Figure 8. Proximity Effect of Cable Conductor ...........................................................................12
Figure 9. A current Icx flows through the insulation material due to the capacitive and
resistive characteristics of the insulation material [20] ..............................................................13
Figure 10. Analogy of electrical and thermal conduction ...........................................................14
Figure 11. Power Triangle ..........................................................................................................21
Figure 12. External Natural Convection to a Cylinder Heat Flux .................................................23
Figure 13. Measurement Set Up for Cable Temperature Development in Ambient
Temperature .............................................................................................................................25
Figure 14. Cable Inside the Temperature Chamber Measurement Set Up .................................26
Figure 15. Simplified Measurement Diagram .............................................................................26
Figure 16. Copper Conductor AC to DC Resistance Ratio ...........................................................28
Figure 17. Aluminium Conductor AC to DC Resistance Ratio ......................................................28
Figure 18. 50 mm2 AC Cable Temperature Development in Horizontal Formation .....................30
Figure 19. 50 mm2 Three Cables Horizontal with 150 A in 20 oC Ambient (FEM Simulation) ......31
Figure 20. 50 mm2 AC Cable Temperature Development in Vertical Formation .........................32
Figure 21. 50 mm2 Three Cable Vertical with 150 A in 20 oC Ambient (FEM Simulation) ............32
Figure 22. 50 mm2 AC Cable Temperature Development in Trefoil Formation ...........................33
Figure 23. 50 mm2 Three Cable Trefoil with 150 A in 20 oC Ambient (FEM Simulation) ..............34
Figure 24. 4 mm2 Three-Cores AC Cable Temperature Development .........................................35
Figure 25. AC Three Phase Multicore Temperature Development (FEM Simulation)..................36
Figure 26. 70 mm2 DC Cable Temperature Development in Horizontal Formation .....................38
Figure 27. 70 mm2 Two Cables Horizontal with 150 A DC in 25 oC Ambient (FEM Simulation) ...38
Figure 28. 70 mm2 Cable Temperature Development Measurement with 150 A in Room
Temperature .............................................................................................................................39
Figure 29. 70 mm2 DC Cable Temperature Development in Vertical Formation .........................40
Figure 30. 70 mm2 Two Cables Vertical with 150 A DC in 25 oC Ambient (FEM Simulation) ........40
Figure 31. 4 mm2 Two-Cores Cable Temperature Development ................................................41
Figure 32. DC Multicore Temperature Development (FEM Simulation) .....................................42
Figure 33. Comparison of Conductor Material in AC Cable Application ......................................44
Figure 34. Comparison of Conductor Material in DC Cable Application ......................................44
Figure 35. Short Circuit Withstand Capability of 50 and 70 mm2 CSA .........................................46
Figure 36. Short Circuit Withstand Capability of 4 and 8 mm2 CSA.............................................47
Figure 37. Short Circuit Withstand Capability for 50 mm2 CSA given various initial conductor
temperature..............................................................................................................................47
Figure 38.Voltage Drop Percentage for 30, 50 and 70 mm2 in DC Application............................49
Figure 39. Voltage Drop for 4 mm2 Two-Core DC Application ....................................................50
Figure 40. Voltage Drop for 50 mm2 AC Cable with various power factor ..................................51
Figure 41. CSA Optimization Flow Chart ....................................................................................52
Figure 42. 70 mm2 AC Cable Temperature Development in Horizontal Formation .....................61
Figure 43. 70 mm2 AC Cable Temperature Development in Vertical Formation .........................61
Figure 44. 70 mm2 AC Cable Temperature Development in Trefoil Formation ...........................62
Figure 45. 4 mm2 Multicore AC Cable Temperature Development .............................................62
Figure 46. 50 mm2 DC Cable Temperature Development in Horizontal Formation .....................63
Figure 47. 50 mm2 DC Cable Temperature Development in Vertical Formation .........................63
Figure 48. 4 mm2 Multicore DC Cable Temperature Development ............................................64
Figure 49. 70 mm2 AC Cable Voltage Drop with Various pf ........................................................64
1
Introduction
In 2017, new electric car sales surpassed a record volume of 1 million units worldwide. This sale included battery electric vehicles (BEVs), plug-in hybrid electric vehicles (PHEVs) and fuel-cell electric vehicles (FCEVs). In 2009, The Electric Vehicles Initiatives (EVI) was established. EVI is a multi-governmental policy forum dedicated to accelerating the deployment of EVs worldwide. Governments consist of the largest and most rapidly growing EV markets worldwide, which are Canada, China, Finland, France, Germany, India, Japan, Mexico, Netherlands, Norway, Sweden, UK and USA. EVI promoted EV30@30, a campaign that setting the collective aspirational goal for all EVI members of a 30% market share for electric vehicles in the total of all vehicles (except two-wheelers) by 2030 [1].
Figure 1. Evolution of the global electric car stock from 2013 to 2017 [1]
Figure 1 displays the increase of EV stock globally since 2013 to 2017 both for Battery Electric Vehicle and Plug-in Hybrid Electric Vehicle around the world. Using New Policies and EV30@30 scenarios, Figure 2 shows a scenario where there will be a significant increase in EV global stock until 2030. With the increasing demand for electric vehicles, a lot of vehicle manufacturers are joining the competition to electrify their vehicles, including SCANIA. The increase of EVs thus increases the needs of on-board electrical components, including cable harness. To be able to compete in this market, the company should be able to innovatively provide both technically fine and affordable products. In the last years, the developing trends in the automotive industry are to provide convenience and safety for the passengers while also competing in terms of weight and energy saving. 10% of weight reduction contributes to 3-4% less fuel average for passenger vehicles or around 5% for heavy-duty vehicles such as trucks and buses [2].
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Figure 2. Global EV stock in the New Policies and EV30@30 scenarios, 2017-30 [1]
The automotive power supply system has great importance regarding the electrical functions and is one of the main factors to reduce manufacturing costs, including the cost of the cable harness [3]. The challenges in vehicle construction are to reduce weight, cut costs, increase efficiency and achieve ever greater functionality while maintaining an increasingly high level of quality. What these challenges mean for wire harnesses in vehicles is that an increasing number of conductors must be accommodated in a very tight space [4]. Cable, as the link between the power supply and the load, requires proper sizing to optimize its function. Correct sizing means to choose the optimum cross-sectional area dependent on various constraints such as ambient temperature, the thickness of insulation, current-carrying capacity, voltage drop allowance and other related things. Thus, it is important that proper cable size is employed in specific applications such as high current circuits for batteries and motors or relatively long cables in bus applications. Applying an improper cable size can cause melting, fire or even explosion.
Inefficiency arises as a consequence of oversizing the conductor. On a positive note, the oversized conductor would ensure a better safety condition for power transmission because with the larger conductor size a higher current is allowed in the cable. For the same length, the resistance value will also be lower than the smaller cable, thus the voltage drop and power loss will be smaller. Nevertheless, there are also many designs and economical downsides to cable oversizing. Large cable takes a lot of space. Compared to static power system cable that usually has wide space which can be utilized, the dynamic electric vehicle does not offer this possibility. The cable should be fit in a more limited space. Thus, having a large cable is not an advantage in terms of system design. Larger cables also increase the total weight of the vehicle. Generally, the heavier vehicle consumes more power. More importantly, larger cable requires more conductor material, which corresponds to higher initial costs of the component. In terms of system design, vehicle total weight and initial costs, the large cable is a disadvantage.
Damage can also occur when the cable is under-sized. Compared to the larger cable, under-sizing conductor certainly offer a better option in terms of easier cable-in-truck system design, lighter weight and lower initial costs. However, under-sizing cable compromises the safety aspects of the vehicle itself. Lower cables mean higher resistance. Higher resistive loss is a major disadvantage for a cable because it will increase the temperature rise of the conductor for the same current flowing in the conductor. The smaller conductor will reach the maximum allowable temperature for the lower current
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compared to the larger conductor. In other words, a smaller conductor causes lower ampacity. The higher resistive loss also means more power required to supply the device, thus decreasing the efficiency of the system. For a specific application, like battery, lower efficiency causes higher usage rate of the battery and will reduce the lifecycle of the component. To minimize the cost, weight and space, while also ensuring the reliability and safety of the system, the optimization process should be implemented.
Therefore, this project is aimed to evaluate different cablesβ designs to find the optimum dimension requirement for Voltage Class B cable in the hybrid electrical vehicle system. Steady-state maximum current or ampacity in various geometries and cable formations will be the main focus. The cross-section area then will also be evaluated with their short circuit withstand capacity and voltage drop.
Trucks and busses will require higher current flowing from the charging component compared to light-weight vehicles. Therefore, investigation of the cable performance is very critical for heavy-duty vehicle. To find the optimum cross-section area, an algorithm needs to be developed to evaluate the optimum favorable cable dimension.
The scope of the project will only be discussed voltage class B cable in the electric vehicle system. As defined in ISO6469-3:2008, Voltage class B is the voltage with a maximum working rms voltage of >30 V and β€ 1000 V in an AC system, or >60 V and β€1500 V in a DC system. The analysis of the cable connectors on both ends will not be included in this project. This project will focus on the optimization of cable material, geometry and configuration. Aluminium is an alternative for conductor material to be considered beside copper in this project. Other complications that arise as the result of choosing aluminium such as special crimping technique will not be included as it is a different topic to address. Analysis of the insulation dimension will also not be included in this project due to broad aspect that it can cover and lack of knowledge on the respective field.
In this project, analytical calculation, finite element method simulation and
measurement are used in combination to find cable ampacity. The reason for using these
three methods is to validate the results of calculation and simulation by conducting
measurement experiments. It could be used to explain the phenomena seen in the
simulation. Simulation offers flexibility to test any type of geometry and formation without
actually building it. The program Comsol Multiphysics is used for the finite element
simulation. Comsol is a finite element analysis, solver and multiphysics simulation software.
It allows computation of physics-based simulation and coupled systems of partial
differential equations (PDEs). Comsol is used because it offers simple physics simulation to
calculate the temperature development in the cable. The analytical method calculation is
developed in Matlab based on IEC 60287 [14, 15], which is the International Electrotechnical
Commission's standard that defines the procedures and equations to be used in
determining the current carrying capacity of cables. The standard is applicable to all ac
cables and to dc cables up to 5kV.
4
Study Literature Review
There are several works that have been carried out before as the foundation of this project. The previous works presented guidance on cable design [5-9], calculated the rise of the conductor temperature as the function of current or ampacity [3, 10-16], voltage drop analysis [3, 5, 7], short circuit assessment [5, 8, 12] and alternative material consideration [2, 17].
In [5] , by Brandon R. Meier and Badrul Chowdhury, a simple method for conductor sizing is explained. It covers conductor loading, ambient temperature, proximity effect, minimum ampacity, fault current capability and voltage drop. However, it does not explain the heat source of the cable, which is the main factor for determining the current loading of the cable. The calculation also more appropriate for a cable with constant low frequency such as power system since it does not take frequency into consideration. The six consideration factors to choose proper sizing are:
a. Circuit Loading. Determine the load of the corresponding circuit is the first step to properly select a conductor. The base ampacity (πΌπππ π) for circuit loading is the minimum current carrying capability of the conductor. Multiplication factors are applied to account for margin to the actual operation of load to cover potential overload or inrush. Typical multiplication factors are provided in Table 1. πΌ is the continuous current that may be available from nameplate information of motors, transformer, chargers, etc. Continuous operation is defined as operation for three or more hours [18].
Table 1. Circuit Loading Multiplication Factors
Load Multiplication Factors [19]
Motor πΌπππ π = 1.25 x πΌ
General-Purpose Transformer πΌπππ π = 1.25 x πΌ
Heaters πΌπππ π = 1.1 x πΌ
Chargers πΌπππ π = 1.25 x πΌ
Motor Control Centers πΌπππ π = β πΌ + 25% Largest Motor
b. The dc resistance of a conductor changes as a result of the ambient temperature
(ππ΄ππ΅). These dc resistance changes affect the value of the ampacity in the conductor. If the ambient temperature increases, the dc resistance increases. Higher dc resistance means higher conductor losses.
c. Proximity Effect (πππΈ). There will be additional heating effects when multiple conductors are close to each other, due to the induction of magnetic fields. A derating factor needs to be applied to account for the increase of the total resistance. Conductor impedance depends on many factors involving conductor itself, conductor spacing and frequency, etc.; therefore, quantifying the electromagnetic field with different configurations is complicated.
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d. Minimum Circuit Ampacity (πΌπππ) is the minimum ampacity of the circuit taking
account of the ambient temperature and proximity effect. e. Fault Current Capability. The heat generated in the cable is proportional to the
square of the current. Due to a very short time of the event before the short circuit is interrupted, the amount of the heat transferred is usually very small. However, in the case when a sustained short circuit happens, the amount of heat transferred from the conductor will increase considerably, and the cable must be dimensioned to preserve its integrity in the worst case.
f. Excessive voltage drop has many negative effects on the electrical systems such as decreased motor torque and reduced pull torque of ac solenoids. General industry practice is to prevent drop exceeding 3 % to the load, or 5 % overall. Voltage drop is found as the product of current and impedance of the circuit (V = IZ). Based on this, the amount of voltage drop can be determined, if the power factor is known.
Another cable sizing method is presented in [7], which includes a study about the effect of cable length on the dynamic performance of an induction motor is also presented. The approach is different compared to [5]; there are four steps to calculate proper techno-economical cable size for a consumer, which are:
1. Determine Cross-Sectional Area Calculation Based on Short Circuit Withstand Capacity Minimum cross-sectional area of cable is determined by the fault current that is flowing,
π = πΌ βπ‘
πΎ
(1)
where π is the nominal CSA of conductor [mm2], π‘ is the fault clearing time [s], πΌ is the fault current [A], and πΎ is factor taking account of the resistivity, temperature coefficient, heat capacity, and initial and final temperatures.
2. Determine Effective Current Carrying Capacity (Thermal Ampacity) This is the maximum current the cable can carry under specified conditions without exceeding the conductor permissible steady-state temperature. In this article, derating or correction factors are applied such as grouping of cables rating (πΆπ) and
ambient temperature factor (πΆπ). 3. Cable Size Selection According to Load Current
In this step, the current flowing in the related conductor is calculated. After considering the derating factors to both load current and short circuit, a larger CSA is chosen.
4. Verification of Cable Size According to Permissible Voltage Drop During Steady-State Operating Condition and Motor Start-Up
This paper [7] provides the main factors to consider when assessing the cable size, and focus heavily on length effect on the voltage drop of the cable. Assessing cable length is important in order to limit the voltage drop in the far end of the cable. In [7], as the cable length increases motor starting current decreases and motor terminal voltage dip increases. Motor starting time also increases with the increase in the length of the cable.
In [8], a simulation-based method to optimize multi-voltage power supply system is presented using an electrical-thermal model to determine ampacity and voltage drop in the cable. There are rating functions that are developed for cable and converter. The factors of
6
evaluation are cost, weight and power loss. Weight and cost of cables are determined by the density of the material. From [8], reducing the conductor size is the main factor to reduce the weight and costs of the cable harness.
This same work [8] developed an algorithm to optimize the cable cross-section area as can be seen in Figure 3. It compares the calculated temperature T as the result of current flowing to the maximally allowed temperature (ππππ₯) and if it meets the requirement, it also compares the minimum voltage (ππππ) requirement. The optimum CSA (π΄πππ‘) should
be reached after implementing this process.
Figure 3. Optimization Process for Cross Sections [8]
In [6], the object of the study is a similar automotive power cable. It researched the problem that may arise due to the use of common shielding in the multicore cable. The focus of the research was about the optimization of cable configuration and material to shielding effectiveness and magnetic compatibility. Temperature development in the cable is a problem in various formations tested in [6]. The temperature development is evaluated in [6] using simulation in Comsol, with variation of the geometry of the AC Cable and DC Cable, the twisting of the cable, shielding material, shielding connection and cable separation.
Aluminium conductors in automotive industry cables are studied in [2, 17]. In [2], the weight reduction of chosen cables is approximately 1.78 kg per truck and 9.67 kg per bus with 40% reduction, thus leading to fuel consumption decrease and environmental advantages.
In [3, 11], different ways of modeling the cable are presented. [11] developed a mathematical model to predict the rise of temperature for a given current in the case of electrical and thermal transient, based on the geometrical subdivision of the structure in several meshes, using Finite Elements Method. [11] studied several methods such as eigenvector (analytical), Runge Kutta, Euler and Crank-Nicolson (numerical methods). From the comparison with the experiment, the results show the maximum error is around 4%.
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All the investigated methods in [3] lead to the same results. Experimental data was also used to validate the result of the model. The three developed models are a direct solution using heat transfer equation, thermal equivalent approach and solution with power flow. The cable was treated as being in free air, with its ampacity restricted by the surrounding ambient temperature. Thus, [3] analyzed cable ampacity in different ambient temperatures and also the heating time to reach pseudo steady state. However, in the calculation and experiment, [3] only used small conductor areas of 0.5 mm2 in free air. Conductor size variation to ampacity and voltage drop that has been simulated in [3] is from 1.5 mm2 to 4 mm2.
In this project, optimization factors affecting cable dimension are derived from the above references. Calculation of factors such as ampacity, voltage drop and short-circuit heating is based directly on the references, and an optimization method is developed using these factors.
8
Cable Properties and Heat Sources
Cable Components
The essential parts of the cables are electrical conductor and insulation. Even though the high voltage of automotive cable is similar to low voltage in the power system, the cable has some differences. During vehicle operation the AC voltage frequency in the cable is not as stationary as in a power system cable in which it is either 50 or 60 Hz: instead, it can go up to more than 600 Hz, depending upon the application. Physically, the automotive cable needs to be more flexible because of the limited space that it has compared to the distribution cable. In most automotive cables, there is no armor layer because it will make the cable difficult to bend. Armor is a steel layer in the cable that provides mechanical protection for the cable. Most of the cables also have a screening layer to reduce the electromagnetic interference. These are some components in the automotive cables (Figure 4):
1. Conductor (Copper or Aluminium), in this project bare stranded 2. Coverage (Tape) 3. Insulation 4. Shielding, tin plated copper braid 5. Wrapping (Tape) 6. Sheath, Outer Insulation
Figure 4. Cable Layers for Single-core
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Figure 5. Two Core Cable Cross Sectional
For multicore cable (Figure 5) shows:
1. Inner Insulation 2. Fillers 3. Shielding 4. Wrapping (tape) 5. Sheath, Outer Insulation 6. Conductor
The two figures above are indicative of single-core and multicore cables for most of the automotive cables. The conductor usually is made from either copper or aluminium due to their high electrical conductivity. The tape is typical of higher voltage cables where it smooths the electric field [20]; it will be ignored in this work. The insulation (both inner and outer) provide protection for the conductor and to prevent short circuit. There are several materials for insulation such as XLPE, PVC, Silicone Rubber, etc. In this project, the inner insulation and the fillers are made of RADOX 155S (extruded and electron beam crosslinked polyolefin copolymer) and outer insulation is RADOX Elastomer (extruded irradiation cross-linked copolymer). Shielding material is tin plate copper braid.
Shielding is used to prevent electrical interference by reducing electromagnetic waves, whether from the protected circuit to other circuits or from other circuits to the protected circuit [9]. The shield works as a blockade between the source of the electromagnetic fields and the areas which need protection from it. In order to reduce the electromagnetic field, thus, a high conductivity material is used in the shielding, such as copper [6]. Shielding also protects the inner insulation and conductor better from damage from outside the cable [9]. The shielding used in this project is tin plate copper braid. Tin is the cheapest coating option for ordinary usage. It has a good corrosion protection and it facilitates the application of solder. Tinβs application is limited to 120 because above this it will oxidize, turning black and corroded [9]. Most of the automotive wires are stranded in order to give flexibility and to improve reliability. For multicore cable, fillers are used to give a cable a smoother construction by supporting the cable outer layer. Filler also gives the inside of the cable a cleaner appearance and strengthens the cable.
10
Heat Sources in the Cable
Heat is generated due to losses in the power cable. Heat in the cable is the limiting factor for a conductor to carry the current. In general, there are four types of losses in the power cable, which are:
1. Conductor Losses (ππ) 2. Dielectric Losses (ππ ) 3. Sheath Losses (ππ ) 4. Armor Losses (ππ)
The losses in the cable can be described using heat equivalent circuit as can be seen in Figure 6. As can be seen in the figure, each layer of the cable is represented by a thermal resistance. In this project, the cable has no armor (ππ = 0), thus it will not be presented in the picture or discussion. Armored cable is mainly used for underground cable or fixed to outdoor wall mounting because armor provides mechanical protection for the cable. The armor reduces the risk of damage to a cable. However, it also increases the cable weight and thus reduces the flexibility of the cable so it will be more difficult to bend, which is a downside for this projectβs application.
Figure 6. Cable Heat Equivalent Circuit
Conductor Losses (ππ)
The main source of heat in the cable is the resistive losses coming from the conductor of the cable. The formula of the resistive or conductor loss is
ππ = πΌ2π
(2)
where πΌ is the current flowing in the conductor [A] and π is the resistance of the conductor at a certain temperature [Ξ©]. The resistance value of the cable is temperature dependent. Thus, dc resistance per unit length of the conductor at operating temperature is given by
π β² = π π[1 + πΌ20(π β 20)] (3)
11
where
π π : the dc resistance of conductor at 20 [Ξ©/m]; πΌ20 : the temperature coefficient [1/K] at 20 . For copper conductor: 3.93 x 10-3, and for aluminium is 4.03 x 10-3 π : the maximum operating temperature [], usually determined by the insulation.
The resistance value usually is given by the manufacturer. In this project, the values of conductor resistivity (π) at 20 for copper conductor is 1.7241 x 10-8 and for aluminium conductor is 2.8264 x 10-8. If AC current flowing through a conductor, there are two other factors that differentiate it from the DC link with regard to the effective resistance, i.e. the power loss in (2). The βAC resistanceβ of a conductor at maximum operating temperature is given by (4) where π¦π and π¦π are factors for skin and proximity effects.
π ππ = π ππ(1 + π¦π + π¦π) (4)
a. Skin Effect (π¦π )
When direct current flows through the conductor, the current is uniformly distributed across the conductor area or current density is the same in all points. However, when alternating current flows in a conductor, it tends to avoid the center of the conductor and flows with higher current density in the peripheral part of the conductor. Thus, the effective total area of current flowing is smaller. Since the resistance is inversely proportional to the effective area of the cable, it will then increase the resistance of the cable, which means higher loss.
Figure 7. Skin effect in AC Conductor (b) compared to DC Conductor (a)
The calculation of skin effect factor (π¦π ) can be seen in the appendix, formula (22), (23), (24) and (25). It depends on the frequency of the AC power, diameter and the experimental skin effect coefficient value that depends on the type of conductor and material. In this study, both stranded copper and aluminium skin effect coefficient value is 1, according to IEC 60287.
The reverse way to understand the skin effect is by considering skin depth. Skin depth is the depth at which the intensity of the material falls to about 37% of its value at the surface. Skin depth is calculated using this formula:
πΏ = β
π
π β ΞΌπ β ΞΌπ β Ο
(5)
12
where ΞΌπ is the relative permeability of the material, ΞΌπ is the permeability of free space (4Ο 10-7 H/m) and π is the resistivity of the material. Since the permeability and conductivity of the material are fixed, the skin depth depends on the frequency.
b. Proximity Effect (π¦π)
The proximity effect is unequal distribution of alternating current over the cross-section of a conductor caused by current in another conductor. It occurs whenever parallel conductors carry alternating current [21]. If the conductors carry the current in the same direction, the magnetic field of the halves of the adjacent conductors are canceling each other which pushes the current to flow more on the away side of the conductor [22]. When the conductors carry the current in the opposite direction, the magnetic fields of the far-off halves of the conductors cancel each other, thus more current flow in the near half side of the conductor [22]. The illustration can be seen in Figure 8. Due to these phenomena, the effective area of the current flow is less, which results in an increase of the wire resistance, and therefore to more power losses in the cable.
DC currents are uniformly distributed and thus there is no proximity effect in the circuit. Frequency, diameter, structure and material are factors affecting the proximity effect. Proximity effect is higher with increasing frequency and diameter. Proximity effect is higher in the material made of higher ferromagnetic material and in solid conductors compared to stranded conductors [22]. The proximity effect factor π¦π for three-core cables
and for three single-core cables, circular conductor can be calculated using formula (26).
Figure 8. Proximity effect of Cable Conductor
Dielectric Losses (ππ )
The dielectric loss is the loss in the insulation material. The cable insulation with the conductor and earthing sheath forms a cylindrical capacitor. The resistive current is flowing through the cable insulation from the conductor to the earthed sheath. This phenomenon can be described by the following figure.
13
Figure 9. A current πΌππ₯ flows through the insulation material due to the capacitive and resistive characteristics of the insulation material [20]
The insulation resistance R is the representative of various losses, which are conductive losses, dipole losses and partial discharge losses. In dc cable with a static electric field, there is no dielectric loss. Hence, it is unnecessary to calculate the dielectric loss for d.c. cable [14].
ππ = π πΆ ππ2 tan πΏ (6)
Here, πΆ is the capacitance per unit length [F/m], ππ is the operating voltage to earth [V] and tan πΏ is the loss factor of the insulation at power frequency and operating temperature.
Dielectric loss is also voltage dependent, thus only important to a certain voltage level related to the insulation material being used [14]. The amount of loss increases quadratically as the voltage level is increased. The dielectric loss should be taken into consideration if the value of ππ equal to or greater than 6000 V [14]. Since the operating voltage applied in this case is less than 1000 V, the dielectric losses factor can be neglected.
Loss factor for sheath and screen (ππ )
Generated magnetic fields induce a current that flow in the earthing sheath. Loss factor in the screen (π1) consists of losses caused by circulating currents (π1
β² ) and eddy currents (π1
β²β²).
π1 = π1β² + π1
β²β² (7)
Circulating current (π1β² ) loss is due to magnetically induced currents. The AC current flowing
in the conductor will induce a voltage in the shield as a parallel metal βloopβ. Likewise, parallel cables will influence each other in all metal loops. Depending on the bonding type of the cable, this induced voltage can cause a current to flow in that loop and this induced current can again influence all other metal loops in the surrounding. If the induced voltage in a certain loop cause a current flowing, there will be losses in the resistance of the metal [20]. In contrast to circulating current, eddy current losses (π1
β²β²) occur for all types of bonding, although they are relatively small. Alternating magnetic fields due to AC current in the cable cause eddy currents in the earthing sheaths [20].
14
Formula (7) expresses the loss in terms of the total power loss in the conductor and indicates which type of loss need to be considered for each particular case [14]. For example, the formula for single-core cables applies to single circuits only and the effects of earth return paths are neglected. For single-core cable with screen bonded at both ends, only loss due to circulating current in the screen needs to be considered. The formula to calculate this loss is presented in Appendix for certain type of formation (29), (31), (32), (33), (38), (39) and (40). Sheath or screen losses are very much dependent on the formation of the cable, bonding arrangement, frequency, sheath and conductor resistance and current in the conductor [23].
Thermal Resistance
When there is a current flowing in the cable, heat is generated in the conductor. The heat can be transferred through the cable by conduction, convection and radiation. Heat produced is then transferred to the surrounding through a medium. This medium has thermal resistance properties which limit the amount of heat that can be released. The schematic of this thermal resistance can be seen in Figure 10. Thermal conductivity indicates how fast heat will flow in a given material [24]. Heat flow can be illustrated as electrical current in the thermal part of the equivalent circuit.
Figure 10. Analogy of electrical and thermal conduction
The thermal equivalent circuit of Ohmβs law can be described as
π1 β π2 = π.π (8)
Here, π1 β π2 is the temperature difference [], π is the heat flow through thermal resistance per unit cable length [W/m] and π is the thermal resistance of material through which current flows per unit cable length.
Metal components of the cable (conductor and shielding) are assumed as a very good heat conductor so the thermal resistance of this material is neglected. The calculation of the ampacity requires a thermal resistance value from the cable properties. For standard circular single-core cable, the thermal resistance calculation is as following
πππ =
Ξπ
πππ =
πππ
2 πln (
ππ ππ
)
(9)
Here, ππ is the outer radius of the material and ππ is the inner radius of the material. From this value, the thermal resistance of other components can be derived.
15
Thermal Resistance of the inner insulation (π1)
π1 is the thermal resistance between conductor and sheath/shielding. This thermal resistance will be different for single-core and multicore cable. Thermal Resistance between one single-core cable conductor and sheath (π1) is given by
π1 =
πT
2 πln [1 +
2π‘1ππ
] (10)
With
πT : the thermal resistivity of inner insulation [K.m/W]
ππ : the diameter of conductor [mm]
π‘1 : the thickness of insulation between conductor and sheath [mm]
Thermal resistance between sheath and Armor (π2)
π2 is not applicable in this project because the cable does not have armor so there is no bedding. Therefore, the value of π2 is equal to zero. Since earthing sheath is a metal part, thermal resistance is neglected. The π2 notation will still be kept like IEC nomenclature.
Thermal Resistance of outer insulation (π3)
Since the layout of the cable is concentric cylindrical layers, (9) is applicable to this part. The thermal resistance of the outer insulation is influenced by thermal resistivity of the insulation material, thickness of the insulation material and the diameter of all the outer cover.
π3 =
πT
2 πln [1 +
2π‘3π·π
] (11)
With πT : the thermal resistivity of outer insulation [K.m/W] π·π : diameter of all layer before the outer insulation [mm] π‘3 : thickness of outer insulation [mm]
External Thermal Resistance (π4)
Heat transfer from the cable will goes through from the conductor to the
surrounding. Thus, the external thermal resistance (surrounding) becomes very important.
In this part, the formation of the cable decides which constant that will be used. Several
possibilities are a stand-alone cable, three cables in horizontal formation, three cables in
vertical formation, three cables in trefoil, two cables in horizontal formation and two cables
in vertical formation. Those configurations are also varied with distance between each
cable. This constants account for the thermal proximity effect of the cable.
For general purpose, the thermal resistance for cable in air and protected from solar
radiation is as follows
π4 =
1
π π·πβ β (βππ )
14
(12)
Where
16
β =
π
(π·πβ)π
+ πΈ (13)
β is the heat dissipation coefficient, using the appropriate values of constant π, πΈ and π given in table 2 in IEC60287-2-1, π·π
β is the external diameter of cable [m] and βππ is the excess of cable surface temperature above ambient temperature. It can be calculated through series of iterative formula or using graphical method provided in IEC60287-2-1 section 5.7.
Conductor Material
The standard choice for electrical conductors for automotive wiring is stranded copper cable. Copper properties of low electrical resistance, high thermal conductivity, physical strength, ease of processing and proven termination techniques are the reasons for choosing copper. However, driven by the need to improve fuel economy and exhaust emission of vehicles which directly related to vehicle weight, alternatives material is being investigated [17]. Aluminium, once again, being investigated as a viable option in this project.
Aluminium has been a key material in engineering for more than 200 years. Aluminium is the lightest of all ordinary metals with a specific mass of 2700 kg/m3. For the same value of electrical conductivity, the weight of aluminium conductor is less than half of the weight of copper conductor. This weight reduction impacts the decrease in fuel consumption and thus CO2 emission [2]. One of the most important facts about aluminium is its plentiful available resource. As a consequence, aluminium price is relatively stable and cheaper compared to copper
On the other hand, copper is the most widely used conductor for electrical purposes. Copper has excellent electrical and thermal conductivity which is very good for power cable so that it can carry high current load. Lower resistivity also means that the total voltage drop, for the same length and cross-section area, will be lower than other metallic conductors [17]. High thermal conductivity material causes easier dissipation for heat. Due to high tensile strength, copper conductor is substantially strong to sustain and withstand mechanical loads and ensure much tension which is beneficial during the installation [2]
The comparison of aluminium and copper properties can be seen in the Table 1Table 2. It displays key properties in order to get a full picture of comparison between aluminium and copper.
Table 2. Normalized Comparison of Copper and Aluminium Properties [17]
Properties Copper Aluminium
Resistivity 1 1,58
Density 1 0,3
Cost (Raw Materials) 1 0,72
Thermal Conductivity 1 0,4
Thermal Expansion 1 1,38
Melting Point 1 0,7
17
Heat Transfer
Heat transfer science seeks to predict the energy transfer which may take place between material bodies as a result of a temperature difference [24]. Similar to current which flows from the higher to lower potential, heat transfer happens between media with different temperatures. Heat transfer is characterized by the following mechanisms:
a. Conduction Heat transfer mechanism is different in different media. For gas, it happens due to collisions of the molecules; for a fluid, through oscillations of each molecule in a cage formed by the neighbors; while in metals, mainly by electrons carrying heat [25]. Energy transferred by conduction is proportional to the normal temperature gradient.
π = βππ΄
ππ
ππ₯
(14)
Here, π is the heat transfer rate, ππ ππ₯β is the temperature gradient in the direction of the heat flow, π is the thermal conductivity of the material [24].
b. Convection Heat convection takes place through the net displacement of a fluid, which transports the heat content in a fluid through the fluidβs own velocity. The convection terms also refer to the heat dissipation from a solid surface to a fluid [25]. The convection effect can be described as
π = β π΄(ππ€ β πβ) (15)
with β is the convection heat-transfer coefficient, ππ€ is the surface temperature and πβ is the temperature of the fluid.
c. Radiation In contrast to the mechanism of conduction and convection where energy is transferred through a material or medium, in radiation the heat may also be transferred into regions where perfect vacuum exists. The heat transferred through electromagnetic radiation as a result of temperature difference [24]. When two bodies exchange heat by radiation, the net heat exchange is then proportional to the difference in π4, thus
π = ν π π΄(π14 β π2
4) (16)
with π is the proportionality constant (Stefan-Boltzmann constant) and ν is the emissivity (absorptive power) which lies between 0 to 1.
18
Ampacity, Short Circuit & Voltage
Drop in the Cable
Ampacity
Ampacity, also known as current-carrying capacity, is the amount of current that can continuously flow through a conductor under certain conditions without exceeding a certain temperature rating [12]. Ampacity is related to electrical and thermal characteristics of a cable. The main source of heat in the cable is the resistive losses coming from the conductor of the cable due to the resistance properties. Controlling the amount of current flowing in the conductor is essential to keep the heat of the cable within the acceptable level.
IEC 60287 [14, 15] is an analysis method to calculate the maximum continuous current flowing in the conductor. IEC 60287 is a parametric study of the major factors affecting ampacity. IEEE std. 60835 is a similar study. Both are based on Neher-McGrath method [16] published in 1957. It is applied to a steady-state conditions, continuous current operation with 100% load factor, to produce the maximum conductor temperature assumed that the ambient surrounding is constant [12]. It is applicable to all AC voltage and DC voltage up to 5 kV.
The ampacity of an AC cable can be derived from the temperature rise above the ambient temperature as follow
βπ = (πΌ2π + 0.5 ππ)π1 + [πΌ2π (1 + π1) + ππ]π π2 + [πΌ2π (1 + π1 + π2) + ππ]π (π3 + π4) (17)
where
πΌ : current flowing in one conductor [A]; βπ : conductor temperature rise above the ambient temperature [K]; π : ac resistance per unit length of the conductor at maximum operating temperature
[Ξ©/m]; ππ : dielectric loss per unit length for the insulation surrounding the conductor [W/m]; π1 : thermal resistance per unit length between one conductor and the sheath [K.m/W]; π2 : thermal resistance per unit length of the bedding between sheath and armor [K.m/W]; π3 : thermal resistance per unit length of the external serving of the cable [K.m/W]; π4 : thermal resistance per unit length between cable surface and surrounding [K.m/W]; π : number of load-carrying conductors in the cable (equal size and carrying the same load); π1 : the ratio of losses in the metal screen to total losses in all conductors in that cable; π2 : the ratio of losses in the armoring to total losses in all conductors in that cable;
From the formula (17), ampacity rating for an AC cable application is obtained as follows
19
πΌ = [
βπ β ππ [0,5 π1 + π (π2 + π3 + π4)]
π π1 + ππ (1 + π1)π2 + ππ (1 + π1 + π2)(π3 + π4)]
0.5
(18)
and the ampacity rating of a DC cable application is as follows
πΌ = [
βπ
π β²(π1 + ππ2 + ππ3 + π π4) ]0.5
(19)
In the above, π β² is the DC resistance per unit length of the conductor at maximum
operating temperature [Ξ©/m]. The differences between AC and DC cable ampacity calculation are the losses. In AC, the conductor losses are dependent on the frequency which causes proximity effect and skin effect in the cable. It causes AC conductor resistance that could be significantly higher than DC resistance. Sheath and screen losses also not applicable in DC application while it increases total losses in the AC application [14].
Short Circuit Current
As mentioned, heat generated in the cable is proportional to the square of current flowing within the conductor. In the normal operation, the steady state current in the cable can flow for long periods in which the cable may reach close to the steady state temperature for the given current. However, during short circuit, the current flowing will be significantly higher, possibly by several or many times. Cables and other equipment are protected from effects of short-circuit by a protection device which will interrupt the current flow according to its setting. One of the most important factors for setting short circuit interruption is the total clearing time or time required to interrupt the short circuit. Since a short circuit is usually interrupted either instantaneously or in a very short time, the amount of heat transferred from the conductors outward to the insulation and other material is small [26]. Therefore, it is important to assess the integrity of the cable insulation. Based on [5], the short circuit capability of a cable can be assessed using
πΌ = π΄ (1.97exp (3)) [0.0297 log (
π2 + 234π1 + 234)
π‘]
1/2
(20)
where
πΌ : short circuit current [A] π΄ : conductor area [mm2] π‘ : total clearing time [s] π1 : conductor insulation temperature [ ] π2 : maximum short circuit temperature []
From (20), there are several factors affecting how much short circuit current are allowed in the circuit, which are
a. Clearing time (π‘)
20
Clearing time is the total time required for the system to clear the circuit from the fault (short circuit current). Extremely high current should be interrupted as soon as possible compared to the lower fault current.
b. Conductor Area (π΄) Since larger CSA means lower resistance, the larger conductor has a better short circuit withstand capacity than the smaller one. It allows higher current flowing in the cable for the same clearing time.
c. Conductor Insulation Temperature (π1) Basically, conductor insulation temperature is equal to the ampacity temperature limit. The inner insulation of the cable is exposed to the heat generated by the conductor inside. Conductor Insulation Temperature is the limit of temperature that the insulation can withstand in steady state condition. The lower the operating temperature would allow higher gap from the cable to reach the maximum short circuit temperature, thus improve short circuit capability.
d. Maximum short circuit temperature (π2) Ampacity is dealing with the steady state condition which means the temperature limitation is specified for the cable to sustain this temperature for as long as possible. Meanwhile, due to thermal resistance, the cable will not be deteriorated instantaneously if the temperature goes above the ampacity temperature limit. Thus, the maximum short circuit temperature is the extreme temperature limit allowable in the cable for relatively short transient time. In this project, the insulation can withstand 250 up to 5 seconds. The higher the short circuit temperature limit, the higher short circuit limit for the cable.
Voltage Drop
Voltage drop is the amount of voltage loss that occurs through certain electrical circuit due to circuit impedance. Important factors affecting voltage drops [7] are
a. Material The lower electrical resistivity is the better material for a conductor because it will provide lower total resistance; thus, lower voltage drops. In general, copper has lower resistivity than aluminium.
b. Conductor CSA Larger cross section area means lower total resistance. Therefore, increasing the size of the cable means reducing the voltage drop in the circuit.
c. Length Since the total resistance is proportional to the length of the circuit, so the longer the circuit, the bigger the total resistance. To provide better voltage at the end side of the circuit, the limitation of the length should be considered.
d. Frequency Frequency affects the total resistance and reactance in the circuit. For AC cable with large CSA, higher frequency cause skin effect and proximity effect which leads to the current flowing in smaller effective area in the conductor. The smaller area, the higher resistance of the cable, thus higher voltage drops.
21
e. Amount of current flowing The higher the design current, the higher the voltage drop.
Power factor (ππ) also affects the voltage drop in the system. Power factor (ππ) is defined as the ratio of the average true or active or effective power in watts to the apparent power in volt-amperes (VA), which is the product of the voltage and current magnitudes in an ac circuit [27]. It is described in Figure 11. A pure resistive load has a ππ of 1. Power factor gives a measure of how effective the real power utilization in the system is. It also represents a measure of distortion of the line voltage and the line current and phase shift between them. In voltage drop calculation, as can be seen in equation (21), the power factor defines how much resistance and reactance of the circuit affecting the total voltage drop.
Figure 11. Power Triangle
Excessive voltage drop is a disadvantage in a power system. In the vehicle, there are a lot of voltage sensitive items of equipment such as inverter and the induction motor. General practice is to limit the voltage drop to a maximum 3% [18]. If the power factor is known, the total voltage drop calculation can be simply put as follow
ππ· = πΌ β πΏ(π cosπ + π sinπ) (21)
where
ππ· : voltage drop in the circuit [V] πΌ : current flowing in the conductor [A] πΏ : length of the conductor [m] π : line resistance for one conductor [Ξ©] π : line reactance for one conductor [Ξ©] π : angle whose cosine is the load pf
Total voltage drop then should be normalized with the supply voltage or voltage at the source to get the percentage of voltage drop along the cable.
22
Simulation Method and Experimental
Setup
Ampacity is a function of temperature as a factor of current flowing in the
conductor. The final conductor temperature limits the cable ampacity. If the final conductor
temperature is set to be higher, then the rise of conductor temperature will be higher too.
Thus, more current is allowed to flow in the conductor. The limitation on the temperature
conductor depends on the insulation thermal ability. In this project, the term ampacity
related to the cable ability to deliver current until the conductor temperature reaches 100
.
The main differences between AC and DC cable applications are the losses. Skin
effect, proximity effect and screen losses happen in AC application while not in the DC
application. All these losses depend on the frequency of the AC power. In this project, the
AC frequency applied is 700 Hz. The AC extra losses calculated in the 6.1.1 will be
implemented to calculate the temperature rise of the conductor given certain current
flowing. For an AC Cable, three conductors are used for three phase current. The
alternatives are three-single conductor in horizontal formation, three-single conductor in
vertical formation, three-single conductor in trefoil formation and three-core cable.
The formation of the cable influences the heat dissipation of the cable. The analytical
method based on IEC 60287 explains this using a heat dissipation coefficient (β). The heat
dissipation coefficient, using the appropriate values of constants π, πΈ and π given in Table 3.
These constants depend on the formation of the cable that are taken directly from IEC
60287-2-1 with some appropriation.
Table 3. Heat Dissipation Coefficient [14]
Number Formation Z E g
1 Two Cables Touching, Horizontal 0.29 2.35 0.5
2 Two Cables Touching, Vertical 1.42 0.86 0.25
3 Three Cables Touching, Trefoil 0.94 0.79 0.2
4 Three Cables Touching, Horizontal 0.62 1.95 0.25
5 Three Cables Touching, Vertical 1.61 0.42 0.2
6 Single Cable, Multicore 1.69 0.63 0.25
23
Simulation Set Up
In Comsol, the physics modules used for modeling formations of more than one
cable are Magnetic Fields, Heat Transfer in Solids and Laminar Flow. These modules are
coupled using the multiphysics menu. Thus, the heat transfer from each cable will be
influenced by the formation of the cables. Since the space around the cable is tight, it is
modelled as a closed off-air domain that represents the space around the cables with a box
surrounding the cable with ambient temperature.
For a single cable (single phase, multicore), the physic modules implemented are
simpler. The airflow around the cable is modeled using convective heat flux from the heat
transfer physic module. The boundary condition βExternal natural convection to long
horizontal cylinderβ is applied to the outer layer of the cable, shown in Figure 12. This model
doesnβt need the non-isothermal flow multiphysics module and laminar flow physics
module, it is a lot less computationally demanding. Both models are running as a transient
simulation with a sufficiently long time, around 10-50 thousand seconds depending on the
conditions, to model pseudo-steady state condition.
Figure 12. External Natural Convection to a Cylinder Heat Flux
Some materials such as copper, aluminium and air are available in the Comsol
library, but others need to be imported manually into comsol user defined library. Radox
155 and REMS properties were imported manually from the manufacturerβs datasheet.
These two are the material of inner and outer insulation for all types of cable. Thin plate
copper braid is the material for cable shielding.
Table 4. Cable Section Material Properties
Material Properties Radox 155 REMS Tin Plate Copper
Electrical Conductivity 4.5 x10-19 [S/m] 8.07 x10-19 [S/m] 7.24 x106 [S/m]
Density 1200 [kg/m3] 1350 [kg/m3] 8960 [kg/m3]
Thermal conductivity and heat capacity for Radox and REMS are temperature
dependent properties. Thermal conductivity and heat capacity data for both materials at
certain temperatures were provided by the supplier, so the Comsol interpolation function
was used to define material property from reading experimental data.
24
In the magnetic fields interface, the βcoilβ feature was added for each conductor.
The current flowing in the conductor then added into the coil setting. In 3 phase AC system,
the currents are equal in magnitude and displaced in phase from each other by 120o. Thus,
the two other phases are multiplied by πβπ2π/3and ππ2π/3. For the mesh setting, the
βextremely fineβ element size of physics-controlled mesh was chosen. Laminar flow physics
was implemented in the air domain inside the box in multi-cable configurations.
Incompressible flow and gravity were put as the physical model in laminar flow setting.
Experimental Set Up
Measurements to observe temperature development of the cable due to DC current
flow were conducted in the laboratory. Measurements were done for 4 mm2 two-core
cable, and for 50 mm2 and 70 mm2 paired single-core cables. Equipment used in the testing
were thermocouples, thermal measurement equipment, temperature chamber, power
source, electrical load and related cables.
The cable measurements were done in two ambient temperature conditions: the
room temperature (25) and the chamber temperature (40). Figure 13 shows the
standard set up to measure the cable temperature development in ambient temperature.
Thermocouples were put inside the cable conductor, on the cable surface and in the air near
the cable. The power source was connected into the electrical load through the cable. The
load was set to control the current flowing in the conductor. The temperature development
was observed on a computer that was connected with the thermocouples using
temperature measurement equipment and its software. The setup of the measurement can
be seen in these pictures. Figure 14 shows the standard set up to measure the cable
temperature development inside a climate chamber. This climate chamber set the initial
ambient temperature for the cable that will be observed. Figure 15 is the simplified
measurement diagram of how measurement in Figure 14 conducted.
25
Figure 13. Measurement Set Up for Cable Temperature Development in Ambient Temperature
26
Figure 14. Cable Inside the Temperature Chamber Measurement Set Up
Figure 15. Simplified Measurement Diagram
27
Result and Analysis
In this chapter, the results of ampacity, short circuit analysis and voltage drop
calculation will be presented to evaluate the proper sizing for each cable application. All
calculations are done for a cable placed in air.
Ampacity Calculation
In order to cross-validate the results, various methods are implemented to analyze
the ampacity of the cable. As in [12], analytical calculation method based on IEC 60287 is
implemented in Matlab script. The results are compared with Finite Element Method
simulation in Comsol and direct testing in Scania Technical Centre. Several sensitivity
analyses are also presented for various factors affecting the ampacity such as the material,
cross-section area, formation, frequency and temperature.
Almost all the properties of the cable were built based on the 70 mm2 automotive
screened cable. When changing the size of the cable, some related properties are adjusted
accordingly. All the cables that are analyzed in this study are shielded cables. Specifically, for
this project, the evaluated areas are 50 and 70 mm2 for single-core cable and 4 mm2 for
multicore cable. DC Cable is applied for all three CSA while AC Cable application is mainly for
50 mm2 cable.
Table 5. General Material Properties
Material Properties Value
Copper Resistivity 1.81 x10-8 [Ω·m]
Copper Constant Mass Temperature Coefficient 3.93 x10-3
Copper Relative Permeability 0.99
Aluminium Resistivity 2.82 x10-8 [Ω·m]
Aluminium Constant Mass Temperature Coefficient 4.03 x10-3
Aluminium Relative Permeability 1
Screen Resistivity 1.39x10-7 [Ω·m]
Losses Calculation
As described in 3.2, there are four main types of losses in the cable and the
conductor loss is the main heat source in the cable. From (4), the difference between AC
and DC cable losses are skin effect and proximity effect. A detailed description of both can
be seen in 3.2.1. Both effects are related to the frequency, material and CSA.
28
Figure 16. Copper Conductor AC to DC Resistance Ratio
In Figure 16, the resistance is higher with higher frequency. In the calculation above,
the conductor final temperature is set at 100 for two single-core copper cable tighten
together. As can be inferred from (22) formula, the skin effect and proximity effect are also
dependent on the dc resistance (π β²) which are related to CSA. For the same length, the
larger CSA has the smaller dc resistance. Resistance is inversely proportional to skin and
proximity effect factor. Thus, the skin and proximity effect are higher in larger conductor.
This phenomenon can also be explained with the skin depth as in (26) formula. Comparing
Figure 16 and Figure 17, Skin and proximity effect for the same conductor size are higher in
copper conductor rather than aluminium conductor due to copper lower electrical
resistivity. However, it does not necessarily mean that aluminium conductor has a lower
total resistance.
Figure 17. Aluminium Conductor AC to DC Resistance Ratio
100
105
110
115
120
125
130
0 50 100 150 200 250 300 350 400 450 500 550 600 650 700
Per
cen
tage
Frequency
AC to DC Resistance Ratio in Various CSA
4
10
30
50
70
100
102
104
106
108
110
112
114
0 50 100 150 200 250 300 350 400 450 500 550 600 650 700
Per
cen
tage
Frequency
AC to DC Resistance Ratio in Various CSA
4
10
30
50
70
29
Table 6. Loss Factor for Screen
Cable Formation Loss factor for screen π1
4 mm2 10 mm2 30 mm2 50 mm2 70 mm2
3 Cores 7.52x10-4 0.0047 0.0419 0.1070 0.1886
3 Single-core Trefoil 3.55x10-3 2.04x10-2 0.1540 0.3583 0.5795
3 Single-core Flat 8.42x10-3 0.0503 0.3966 0.9064 1.3972
The formula to calculate the loss factor for sheath and screen can be seen in (29),
(33) and (38). Only three cores and three single-core cables are calculated because the loss
is only applied for AC cable application. The results in Table 6 are calculated for maximum
conductor temperature at 100 , copper conductor material and 700 Hz frequency. The
results show that the higher the CSA, the higher loss factor for sheath and screen. Three
single-core cables in flat formation have a higher loss factor compared to trefoil formation
or a three-core cable. These loss factors were used in the ampacity calculation as the ratio
to total conductor losses in that cable. The higher loss factor corresponds to the higher total
loss in the cable, thus higher temperature increases for the same current.
30
AC Ampacity Result
In this part, temperature development of three single-core cables laid in horizontal,
vertical and trefoil formation is presented. Three-cores cable with 4 mm2 CSA is also
presented.
Figure 18. 50 mm2 AC Cable Temperature Development in Horizontal Formation
31
Figure 19. 50 mm2 Three Cables Horizontal with 150 A in 20 oC Ambient (FEM Simulation)
Table 7. Comparison of Temperature Development Calculation in AC Horizontal Formation
Method AC Current [A] Conductor Temperature []
T ambient = 20 T ambient = 40
Analytical Method (IEC)
100 47.4 68
150 74.8 96.1
FEM Simulation (Comsol)
100 35.7 57.6
150 53.6 77.4
32
Figure 20. 50 mm2 AC Cable Temperature Development in Vertical Formation
Figure 21. 50 mm2 Three Cable Vertical with 150 A in 20 oC Ambient (FEM Simulation)
33
Table 8. Comparison of Temperature Development Calculation in AC Vertical Formation
Method AC Current [A] Conductor Temperature []
T ambient = 20 T ambient = 40
Analytical Method (IEC)
100 45.2 65.8
150 70.5 91.7
FEM Simulation (Comsol)
100 34.3 55.1
150 49 70.8
Figure 22. 50 mm2 AC Cable Temperature Development in Trefoil Formation
34
Figure 23. 50 mm2 Three Cable Trefoil with 150 A in 20 oC Ambient (FEM Simulation)
Table 9. Comparison of Temperature Development Calculation in AC Trefoil Formation
Method AC Current [A] Conductor Temperature []
T ambient = 20 T ambient = 40
Analytical Method (IEC)
100 44.2 64.9
150 68.7 90.3
FEM Simulation (Comsol)
100 35.5 56.4
150 52.1 73.8
35
Figure 24. 4 mm2 Three-Cores AC Cable Temperature Development
Table 10. Comparison of Temperature Development Calculation in AC Multicore Cable
Method AC Current [A] Conductor Temperature []
T ambient = 20 T ambient = 40
Analytical Method (IEC)
20 36.2 57
30 53 75.4
40 77.5 101.2
FEM Simulation (Comsol)
20 40.2 62
30 60.4 84.2
40 89.3 116
36
Figure 25. AC Three Phase Multicore Temperature Development (FEM Simulation)
There are significant differences between the analytical method based on IEC 60287
calculation and the FEM simulation in Comsol. The absolute difference between both
methods ranges from 4 up to 37 . The IEC analytic method tends to overestimate the
cable loss in the screen factor calculation as described in [28]. In [10], the analytical method
produces optimistic results when it applies to a different condition than the designated
environment. In other work [29], the FEM Comsol Simulation was found to slightly
underestimate the heat transfer calculation. The gaps between both calculations is
significant at higher frequency. At zero frequency, the results show a very close value.
Graphics and pictures for other areas can be seen in Figure 42, Figure 43, Figure 44 and
Figure 45.
From Figure 18, Figure 20 and Figure 22, the ampacities of the cables are
summarized in Table 11. Three cables in trefoil have higher ampacity compared to
horizontal and vertical formation. Since the cables implemented are identical, this
difference happened due to the formation. Cables in trefoil formation have a better heat
dissipation coefficient which represents this formationβs ability to release heat into the
ambient. The ampacity is taken from the hottest conductor out of the three. In a three-
phase system, this conductor is the limiting factor for the cable delivering more current.
37
Table 11. AC Cable Ampacity
CSA [mm2] Type Formation Ampacity [A]
Ta = 20 Ta = 40 Ta = 60 Ta = 80
4 Multicore 47 39 31 20
50 Single-Core
Horizontal 185 155 121 79
Vertical 194 163 127 83
Trefoil 197 165 129 84
70 Single-Core
Horizontal 199 167 130 85
Vertical 207 174 136 89
Trefoil 219 184 143 94
The maximum ampacity difference between the presented formations is up to 20 A.
For the 50 mm2 and 70 mm2 CSA, the maximum ampacity difference due to cable formation
is stable around 6 % and 9% for all ambient temperature. Horizontal formation has the
lowest ampacity due to the limitation of the cable in the middle. Heat flow is proportional to
the surface area according to (14), (15) and (16) equations. In horizontal formation, the
middle cable is trapped by other conductors in the left and right so that the effective area to
release the heat is decreasing.
Vertical formation has a better heat dissipation than the horizontal one because the
limitation factor, the conductor on the top, has a wider effective surface area to dissipate
heat. Trefoil cable formation also has a better heat dissipation than the horizontal one
because the heat is dissipated more balance by all three conductors. Table 6 shows that the
loss factor for the screen in trefoil formation is smaller than the flat formation which affect
the total loss in the system. However, for cable installation in a complex and tight place such
as truck chassis, the formation of the cable might be changing along the line, in which case it
is important to consider the lowest ampacity as the cable ampacity.
Heated air rises because it is less dense compared to the colder air around, as can be
seen in Figure 19, Figure 21 and Figure 23. In Figure 19, the middle cable is the hottest one
because it has the smallest area to dissipate the heat since it is blocked by other cables.
Figure 25 is the example of temperature development simulation result performed by
Comsol for multicore cable. It applied convective heat flux from the heat transfer physic
module which is simpler than more than one cable formation. The outer layer of the cable is
simulated using βexternal natural convection to long horizontal cylinderβ boundary
condition. Thus, it will assume an isothermal outer environment of the cable.
DC Ampacity Result
a. Two Cables Touching Horizontally
38
Figure 26. 70 mm2 DC Cable Temperature Development in Horizontal Formation
Figure 27. 70 mm2 Two Cables Horizontal with 150 A DC in 25 Ambient (FEM Simulation)
39
Figure 28. 70 mm2 Cable Temperature Development Measurement with 150 A in Room Temperature
Table 12. Comparison of Temperature Development Calculation for DC in Horizontal Formation
Method DC Current [A] Conductor Temperature []
T ambient = 25 T ambient = 40
Analytical Method (IEC)
150 40.9 56.6
200 51.2 67.3
FEM Simulation (Comsol)
150 40.4 55.3
200 51.7 67.2
Experiment 150 39.3 47.9
200 51.4 55.1
40
Figure 29. 70 mm2 DC Cable Temperature Development in Vertical Formation
Figure 30. 70 mm2 Two Cables Vertical with 150 A DC in 25 Ambient (FEM Simulation)
41
Table 13. Comparison of Temperature Development Calculation for DC in Vertical Formation
Method DC Current [A] Conductor Temperature []
T ambient = 25 T ambient = 40
Analytical Method (IEC)
150 40.2 55.8 200 50.2 66.5
FEM Simulation (Comsol)
150 39.9 54.9 200 50.3 65.9
Figure 31. 4 mm2 Two-Cores Cable Temperature Development
42
Figure 32. DC Multicore Temperature Development (FEM Simulation)
Table 14. Comparison of Temperature Development Calculation for DC Multicore Cable
Method DC Current [A] Conductor Temperature []
T ambient = 25 T ambient = 40
Analytical Method (IEC)
20 37.1 52.7
30 49.8 66
40 67.3 84.3
FEM Simulation (Comsol)
20 40.4 56.4
30 55.7 72.8
40 76.3 94.7
Experiment
20 36.4 46.5
30 47.7 55.3
40 70.2 69.2
Different from AC calculation, the temperature development calculation for DC cable
application is almost identical in all three methods. At the room temperature (25 oC), the
difference between the calculated value in analytical method compared to the
measurement is very small, around 0.2 oC to 2.5 oC or less than 5%. FEM simulation also
provides a close result with the absolute temperature difference around 0.2 to 2.4 oC (1% to
4% error), similar to analytical method. The analytical method showed this consistency for
various CSA. For temperature development of multicore cable, the analytical method has a
better approach than FEM simulation: the simulation has an absolute 8 oC temperature
difference, around 15%, at 30 A. However, the temperature development is not linear, and
this error value reduces at the higher or lower currents.
43
At 40 ambient temperature setting, measurements made in the chamber showed
a worse deviation from calculation and simulation than was seen at room temperature. In
two-cables formation with 50 and 70 mm2 CSA, the absolute error for the analytical method
and also FEM Simulation is around 5 to 12 , i.e. 15-20% relative error. For the 4 mm2 CSA
multicore cable, FEM simulation has a worse error, around 20-30 %. This error is likely
caused by the temperature setting in the chamber where it has a fan that took the heat
away so that it can keep the chamber temperature steady at designated 40 . Even though
the fan has been covered with an internal box, the indirect fluid may still be affecting the
cable. See the last row of Table 12, the 25 and 40 ambient temperature difference for
70 mm2 cable with 200 A current flowing is only 3.7 oC. In Table 14, the 4 mm2 multicore
cable with 40 A current has a higher conductor temperature (70 to 69.2 ) in 25
ambient temperature than the 40 chamber temperature.
Table 15. DC Cable Ampacity
CSA [mm2] Type Formation Ampacity [A]
Ta = 25 Ta = 40 Ta = 60 Ta = 80
4 Multicore 53 46 36 24
50 Single-Core Horizontal 280 245 192 126
Vertical 284 249 195 128
70 Single-Core Horizontal 347 304 238 157
Vertical 353 309 243 160
Ampacity of the cables from Figure 26, Figure 29 and Figure 31, are summarized in
Table 15. Similar to AC simulation, the cable in the horizontal formation has a lower
ampacity compared to the vertical formation which means it has a higher loss in the cable.
In vertical formation, the limitation factor is the upper cable where the heat from the lower
cable goes up and increases the amount of heat that needs to be released. For the
horizontal cable, both conductors are heated equally. Vertical formation has a slightly better
heat dissipation coefficient.
The difference in the ampacity is not as big as in an AC cable application. For the 50
mm2 CSA, the ampacity difference between horizontal and vertical is around 3 A or 1.5 %.
For 70 mm2 CSA, the ampacity different is 5 A or 1.7%. Considering the complexity of the
cable routing, it is good to consider the lowest ampacity as the main ampacity.
Figure 28 is an example of typical result shows in the computer when performing the
temperature development measurement. There are three curves which represent three
different temperature measurement. The red one is the temperature development inside
the conductor, the orange represent the temperature development at the jacket of the
cable while the other one is the ambient temperature. Ambient temperature was generally
stable at 25 while other two parameter rose up as the current increased.
Figure 32 is the example of temperature development simulation result performed
by Comsol for dc multicore cable. It applied convective heat flux from the heat transfer
physic module which is simpler than more than one cable formation. The outer layer of the
cable is simulated using βexternal natural convection to long horizontal cylinderβ boundary
condition. Thus, it will assume an isothermal outer environment of the cable.
44
Conductor Material Comparison
Figure 33. Comparison of Conductor Material in AC Cable Application
Figure 34. Comparison of Conductor Material in DC Cable Application
Figure 33 and Figure 34 show the comparison between copper and aluminium as
conductor material in both AC and DC application. For AC application, although the skin
45
effect has greater impact on copper conductor, the overall resistance of the copper
conductor is still lower than aluminium conductor. This applied to 700 Hz, with 70 mm2 CSA.
For smaller CSA, the skin effect would be reduced as can be seen in Figure 16. To reach 100
from 20 ambient, the copper allowed 199 A while aluminium allowed 182 A.
For DC application, the skin effect is not relevant. The ampacity of the 70 mm2 cable
in 25 ambient temperature is 347 A for copper and 277 A for aluminium. Even more,
from Figure 34, copper at 60 ambient has higher ampacity than aluminium at 25
ambient if the conductor temperature set above 140 .
46
Short Circuit Calculation
The important variables for maximum short circuit current evaluation are the cross-
section area of the cable, the conductor operating temperature, the maximum short circuit
temperature and clearance time. Since the insulation material is crosslinked thermoplastic
polymer (RADOX), it can withstand short circuit temperature up to 250 for 5 seconds.
The conductor temperature is the temperature when the conductor is operated at its
ampacity, which is 100 in this case.
Figure 35. Short Circuit Withstand Capability of 50 and 70 mm2 CSA
Figure 35 and Figure 36 shows cable short circuit withstand capability from 0.1 to 5
seconds for various CSA. The larger the CSA, the higher the short-circuit current that is
allowed for the same clearance time. The larger the CSA, the longer fault duration the cable
can withstand. For duration less than about 0.5 s, a small change in duration such as 0.1 s
can make a substantial change to the maximum permitted short-circuit current. Figure 37
shows the short circuit withstand capability given various initial conductor temperature
conditions. The higher the initial conductor temperature, the lower the cable short circuit
withstand capability due to a smaller temperature gap to reach maximum short circuit
temperature, 250 .
47
Figure 36. Short Circuit Withstand Capability of 4 and 8 mm2 CSA
Figure 37. Short Circuit Withstand Capability for 50 mm2 CSA given various initial conductor temperature
Short circuit withstand capability of a cable does not change linearly with time. From Figure
35 and Figure 36, after 0.5 seconds there is a big decrease in how much short circuit current
are able to be handled by the cable. From 0.1 s to 0.5 s, the short circuit current is
decreased by more than 50%. Another 50% reduction is happened from 0.5 s to 2 s. It is
48
crucial to check on how much the short circuit current can flow in the cable and how long it
takes for the protection system to isolate the fault. Those two criteria are the reason behind
choosing the correct CSA. The summary from short circuit withstand capability figure can be
seen in the table below.
Table 16. Short Circuit Withstand Capability of a Cable
duration [s]
Short Circuit Withstand [kA]
Cross-Section Area
4 mm2 8 mm2 20 mm2 50 mm2 70 mm2
0.1 2.6 5.2 13.1 32.7 45.8
0.25 1.65 3.3 8.2 20.7 29
0.5 1.1 2.3 5.8 14.6 20.5
2 585 [A] 1.1 2.9 7.3 10.2
5 370 [A] 741 [A] 1.8 4.6 6.4
49
Voltage Drop Calculation
Voltage drop in the cable depends on three important factors. From equation (21),
the cable impedance, cable total length and the current flowing in the conductor are factors
to consider for correct sizing of the cable. For AC application, the power factor also affects
the composition of resistance and reactance in total impedance. Frequency also is relevant
in AC cable application because it changes the resistance value due to skin and proximity
effects.
Figure 38.Voltage Drop Percentage for 30, 50 and 70 mm2 in DC Application
The chosen ampacity as the current flowing in the calculation is the highest between
those three formations in AC or two formations in DC. In the calculation, the voltage that is
used as base voltage for AC is 650 Vrms and for DC is 660 V. Figure 38 shows the cable length
effect to the voltage drop of 30, 50 and 70 mm2 cable. Each cable has the current flowing in
its conductor as much as the ampacity from 25 room temperature to 100 so that the
resistance value is at 100 . The maximum length for those cables to keep the voltage drop
below 3% is presented in Table 17.
50
Table 17.Maximum Length of DC Application Cable
Formation CSA [mm2] Maximum Length [m]
Single-Core
70 83
50 74
30 60
Two-Cores 4 31
Figure 39. Voltage Drop for 4 mm2 Two-Core DC Application
Figure 39 shows the voltage drop magnitude for 4 mm2 two-Core DC cable on its
ampacity. Depending on the type of voltage applied in the cable, the 3% voltage drop limit
can be varied. For the same 660 V, the maximum 4 mm2 two-core cable length to limit the
voltage drop is 31 m in order that the voltage drop magnitude is not more than 19.8 V. A
difference when calculating DC and AC cable application is that the equation (21) is
multiplied by 2 in a DC application to account for the conductor length from the source to
the load (+) and from the load back to the source (-), whereas for three phase AC application
the equation should be multiplied by β3.
Voltage drop of 50 mm2 AC cable at various power factor is described in Figure 40.
For 50 mm2 AC cable, the worst voltage drop happens when the pf = 0.55. This means that
for this cable, pf value of 0.55, the impedance is at the highest compared to other pf values.
For 50 mm2 AC cable, at 0.55 pf, the maximum length should be 61 meters while if the pf
value is 1, the maximum length can go up to 105 meters. The reactance value affects the
total impedance due to this power factor. In the automotive power system, the power
51
factor would vary depending on the application. Thus, it is important to consider all the
possible pf when assessing maximum length of the AC cable.
Figure 40. Voltage Drop for 50 mm2 AC Cable with various power factor
52
Cable Optimization Process
This chapter elaborates steps that need to be taken to obtain the smallest possible cable cross-section area from technical point of view. The optimization process is explained step by step with this flow chart.
Figure 41. CSA Optimization Flow Chart
CSA Optimization Flow Chart in Figure 41 describes steps to choose the smallest CSA that is still technically reliable. These steps would save the initial investment cost of the cable. Cable CSA optimization process is divided into three important steps, which are
53
A. Choosing CSA based on the current flowing in the conductor
1. As described in Figure 41, the first step is collecting all the data and the standard
required to calculate the temperature development which are initial CSA (An),
current flowing in the circuit, frequency, ambient temperature, maximum
conductor temperature, short circuit profile in the circuit (current and duration).
2. For certain initial CSA, current and ambient temperature, calculate the final
conductor temperature.
3. If the final conductor temperature (π) is lower than the standard maximum
conductor temperature (ππππ₯), decrease the cable CSA until the final conductor
temperature is equal to or slightly lower than the maximum conductor
temperature.
4. Otherwise, if the final conductor temperature is higher than the standard
maximum conductor temperature, increase the cable CSA until the final
conductor temperature is equal to or slightly lower than the maximum conductor
temperature.
5. If the final conductor temperature is equal to maximum conductor temperature,
continue to the next step.
B. Short-Circuit Evaluation
6. Calculate short circuit capability for related cable.
7. Compare the short circuit current (Isc) and time in the related cable protection
setting to the calculated short circuit capability (SCC).
8. If the short circuit or fault current in the cable is higher than the cable short circuit
capability, increase the cable CSA.
9. If the short circuit or fault current in the cable is lower than or equal to the cable
short circuit capability, continue to the next step.
C. Voltage Drop Calculation
10. Calculate the voltage drop for the cable with its specific length.
11. If the cable voltage drop is more than 3%, increase the cable CSA.
12. If the voltage drop is less than 3%, then the cross-section area is the most optimal
CSA for this circuit.
54
Conclusion
Ambient temperature, maximum permitted conductor temperature, and total losses
generated in the cable are factors affecting the ampacity. Cable sections can be located
through different ambient temperatures; thus, it is important to choose the highest ambient
temperature the cable has to go through in order to cover the weakest link in the cable. The
highest temperature was set to 100 in this study, to maximize the temperature rise while
not unduly reducing the cablesβ expected lifetime.
In three-phase AC power applications with three cables, trefoil is the best formation
to maximize cable ampacity. For example, for 50 mm2 CSA with 700 Hz frequency, trefoil
cable formation ampacity in 20 ambient temperature is 197 A. For the same parameter,
horizontal formation ampacity is 185 A and the vertical formation is 194 A. On average, the
ampacity difference due to cable formation is around 6 to 9%. In trefoil formation, the heat
is evenly distributed in all three cables. Meanwhile, in horizontal and vertical formation, the
cable in the middle or the top will continuously receive higher heat than the others, and so
will wear out faster than the other two cables. Therefore, trefoil formation is the most
recommended formation for three-cables AC application.
In two-cables DC application, the vertical formation has a better ampacity than the
horizontal one. For example, in 70 mm2 CSA, the vertical formation ampacity in 25
ambient temperature is 353 A while the horizontal formation ampacity is 347 A. On average,
the ampacity difference between horizontal and vertical formation is less than 2%. For DC
application, heat distribution is better in the horizontal formation than the vertical
formation. Both left and right conductors are exposed to the same amount of heat. In the
vertical formation, the conductor in the upper position receives higher heat compared to
lower conductor. Thus, in DC current application, vertical formation provides higher
ampacity.
There are significant differences between the analytical method based on IEC 60287
calculation and the FEM simulation in Comsol. The absolute difference between both
methods ranges from 4 up to 37 . The IEC analytic method tends to overestimate the
cable loss in the screen factor calculation. Different from AC calculation, the temperature
development calculation for DC cable application is almost identical in all three methods. At
the room temperature (25 ), the difference between the calculated value in analytical
method compared to the measurement and simulation is very small, around 0.2 to 2.5
or less than 5%. Further investigation needs to be done to get deeper understanding.
Short-circuit withstand capability of a cable depends on the CSA, maximum short
circuit temperature, conductor temperature and time required to clear the fault. 500 ms is
the critical time for the short circuit calculation because there is a significant difference
between short circuit withstand capability before and after this time. The protective device
55
that protects the cable should be able to clear the fault faster than the maximum permitted
clearance time for the short circuit current in the cable.
Voltage drop calculation is assessed to limit the cable length so that the voltage at
the load end side does not vary unreasonably much. In DC application, voltage drop only
depends on the total resistance and length of the cable while in AC, it depends on total
impedance and power factor. For automotive cable applications, voltage drop is not a
significant factor.
56
Future Work
The following is an indication of future works that can be done to complement the
work done in this project. Since the gap between the IEC analytical method and the
simulation result for AC application was substantial, the cable should be tested directly in
the laboratory. In order to observe the influence of frequency on the skin effect, proximity
effect and screen losses, a three-phase current generator and frequency controller are
required. The testing result would verify which method is the best option to calculate
temperature development in AC application.
The cable designs tested in this project were based on actual and standard cable
layouts that can be implemented in a vehicle right now. It is recommended to simulate
other various types of formation and cable design to deepen the understanding of the cable
formation and design effect. Various cable designs that can be investigated are shaped-
conductor, DC four-core cables, AC six-core cables, etc. Many types of cable formation,
especially if the multicables for the same phase will be used, can also be simulated such as
trefoil with circular arrangement of the cable, six horizontal cables, rectangular or square
shaped formation of the cable, etc.
Study of the Voltage Class B insulation part might also be required. The insulation
material and its thickness affect the cable thermal resistance and the safety standards of
the cable. The insulationβs ability to withstand high temperature is also critical because it is
the limiting factor of the cableβs ampacity which is also related to cable expected lifetime.
The insulation material and thickness will also affect other mechanical properties of the
cable such as bending ratio and total weight.
57
Appendix
Formula
The calculation of skin effect factor (π¦π ) is given by the following equations:
For 0 < π₯π β€ 2.8
π¦π = π₯π
4
192 + 0.8 π₯π 4
(22)
For 2.8 < π₯π β€ 3.8 π¦π = β0.136 β 0.0177π₯π + 0.0563π₯π
2 (23)
For π₯π > 3.8 π¦π = 0.354π₯π β 0.733 (24)
where
π₯π 2 =
8ππ
π β²10β7ππ
(25)
π : the supply frequency [Hz] ππ : experimental skin coefficient value depends on the type of cabling. In this study, stranded copper and aluminium cable is 1.
The calculation of proximity effect factor (π¦π) is given by the following equations:
π¦π =
π₯π4
192 + 0.8 π₯π4(ππ
π )
2
[
0.312 (ππ
π )
2
+1.18
π₯π4
192 + 0.8π₯π4 + 0.27
]
(26)
π₯π2 =
8ππ
π β²10β7ππ
(27)
ππ is the diameter of the conductor [mm], π is the distance between the conductor axes [mm] and ππ is the experimental proximity coefficient value depends on the type of cabling.
In this study, the value is 1 for stranded copper conductor and solid aluminium conductor while 0.8 for stranded aluminium conductor.
The calculation of capacitance for cylindrical conductors is given by a
πΆ =
ν
18 ln (π·i
πc)10β9
(28)
where
ν : relative permittivity of the insulation π·i : external diameter of the insulation (excluding screen) [mm] πc : diameter of conductor, including screen if any [mm]
58
The Calculation of Loss Factor for Screen Losses
For two single-core cables and three single-core cables (triangle) with screen bonded at both ends, the loss factor is given by
π1β² =
π π
π
1
1 + (π π
π )2 (29)
where
π π : resistance of the screen per unit length of cable at maximum operating
temperature [Ξ©/m];
X : reactance per unit length of screen of cable [Ξ©/m];
π = 2 π 10β7ln (2π
π) (30)
π : the distance between conductor axes in the electrical section being considered [mm] π : mean diameter of the screen [mm] π1
β²β² : 0, eddy current is ignored.
For three single-core cables in flat formation, with the middle cable equidistant from the outer cables, without transposition and with the sheaths bonded at both ends, the loss factor for the outer cable carrying the lagging phase is
π11β² =
π π
π [0.75π2
π π 2 + π2
+0.25π2
π π 2 + π2
+2 π π π πππ
β3(π π 2 + π2)(π π
2 + π2)]
(31)
For the other outer cable, the loss factor is
π13β² =
π π
π [0.75π2
π π 2 + π2
+0.25π2
π π 2 + π2
β2 π π π πππ
β3(π π 2 + π2)(π π
2 + π2)] (32)
For the middle cable, the loss factor is
π12β² =
π π
π
π2
π π 2 + π2
(33)
In this formula:
π = π + ππ (34)
π = π βππ
3 (35)
where
59
π = 2 π 10β7ln (2π
π)
(36)
is the reactance of screen per unit length of cable for two adjacent single-core cable [Ξ©/m];
πm = 2 π 10β7ln(2)
(37)
is the mutual reactance per unit length of cable between the sheath of an outer cable and the conductors of the other two when the cables are in flat formation. Eddy current loss π1
β²β² is ignored.
For two core unarmored cable where the cores are contained in a common metallic sheath, circulating current loss (π1
β² ) is negligible and the loss factor for round conductors is
π1β²β² =
16 π210β14
π π π (π
π)2
[1 + (π
π)
2
] (38)
where
c : distance between the axis of one conductor and the axis of the cable [mm] d : mean diameter of the sheath [mm]
For a three-core unarmored cable where the cores are contained in a common metallic sheath, circulating current loss (π1
β² ) is negligible and the loss factor for round conductors is
- for π π less than or equal to 100 πΞ©/m
π1β²β² =
3 π π
π [(
2π
π)
2 1
1 + ( π π π 107)
2 + (2π
π)
4 1
1 + 4 ( π π π 107)
2]
(39)
- for π π greater than 100 πΞ©/m
π1β²β² =
3.2 π2
π π π (2π
π)
2
10β14
(40)
Calculation of Thermal Resistance of the Inner Insulation (π1)
For two core belted cables with circular conductors
π1 =
πT
2 ππΊ
(41)
where
G : Geometry factor that depends on the thickness of insulation between conductors
(π‘), thickness of insulation between conductors and sheath (π‘1) and diameter of the
conductor (ππ). The value is given on IEC60287-2-1, Figure 2.
For three core belted cable with circular conductors
60
π1 =πi
2 ππΊ + 0.031(ππ β πi)π
0.67π‘1ππ (42)
where
πi : thermal resistivity of the insulation [K.m/W];
πi : thermal resistivity of the filler material [K.m/W]
The geometric factor is given in figure 3 of the IEC60287-2-1
Calculation of External Thermal Resistance (π4)
πΎπ΄ = π π·π
β β
(1 + π1 + π2)[π1
π+ π2(1 + π1) + π3(1 + π1 + π2)]
(43)
Then
(Ξππ )π+11/4
= [Ξπ + Ξππ
1 + πΎπ΄(Ξππ )π1/4
]
0.25
(44)
Set the initial value of (βππ )1
4 = 2 and reiterate until (Ξππ )π+11/4
β (Ξππ )π
1
4 β€ 0.001. If Ξππ =
0 if dielectric losses are neglected.
61
Figure
AC Ampacity
Figure 42. 70 mm2 AC Cable Temperature Development in Horizontal Formation
Figure 43. 70 mm2 AC Cable Temperature Development in Vertical Formation
62
Figure 44. 70 mm2 AC Cable Temperature Development in Trefoil Formation
Figure 45. 4 mm2 Multicore AC Cable Temperature Development
63
DC Ampacity
Figure 46. 50 mm2 DC Cable Temperature Development in Horizontal Formation
Figure 47. 50 mm2 DC Cable Temperature Development in Vertical Formation
64
Figure 48. 4 mm2 Multicore DC Cable Temperature Development
Voltage Drop
Figure 49. 70 mm2 AC Cable Voltage Drop with Various pf
65
66
Matlab Code
Ampacity Calculation
%% AMPACITY CALCULATION BASED ON IEC60287-1-1 and IEC60287-2-1
clear all
clc
%% PARAMETRIC SWEPT
A_con = [50]; %cross section [mm2]
T_start = [25 40 60 80];%ambient temperature [degC]
s_con_axis = [0]; %separation of cable [mm]
material = [1 2]; %1=COPPER, else = ALUMINIUM
T_con = [20:160]; %Temperature end variable[deg C]
%% CONTROL VARIABLE
TR1Factor = 1; %Factor to calculate T1
%1 = single-core - AC & DC
%2 = 2 core belted cables - multicore DC
%3 = 3 core belted cables - multicore AC
n = 1; %number of conductors in a cable, so either 1, 2 or 3
f = 0;
formationtype = 2; %Factor to Calculate T4
%1 = DC touching horizontal %2 = DC touching vertical
%3 = DC space horizontal %4 = DC space vertical
%6 = AC touching horizontal %7 = AC touching vertical
%8 = AC space horizontal %9 = AC space vertical
%5 = AC touching trefoil %10 = single cable (multicore)
%%space mean = 1 D
typeofssloss = 3; %Sheat Screen Losses
%1 = AC-3ph-Trefoil,
%2 = AC-3ph-Flat,
%3 = AC-3cores,
%% LOOP
for cc = 1:length(material);
for aa = 1:length(A_con);
for bb = 1:length(T_start);
for dd = 1:length(s_con_axis);
for ee = 1:length(T_con);
%% GENERAL
omega = 2*pi*f;
T_0 = T_start(bb)*1; %Ambient Temperature
T_end = T_con(ee); %Max Conductor Temperature
if T_end > T_0
dT = T_end-T_0;
else
dT = 0;
end
u0 = 4*pi*10^(-7); %Permeability of free space
%% GEOMETRY
Acon = A_con(aa)*10^(-6); %cross section [m2]
rcon = sqrt(Acon/pi); %radius of conductor [m]
dcon = 2*rcon; %diameter of conductor [m]
t_ins1mm = 1.77; %thickness of inner insulation [mm]
t_ins1 = t_ins1mm*10^(-3); %thickness of inner insulation [m]
67
d_ins1 = dcon+(2*t_ins1); %diameter of insulation [m]
t_smm = 0.55; %thickness of shield [mm]
t_s = t_smm*10^(-3); %thickness of shield [m]
if n == 1; %mean diameter of the screen [m]
d_s = d_ins1+(2*t_s);
elseif n == 2;
d_s = (2*d_ins1)+(2*t_s);
elseif n == 3; %use equilateral triangle
d_s = 2*((d_ins1/sqrt(3))+0.5*d_ins1) + (2*t_s);
end
d_cc = d_ins1/sqrt(3); %distance between axes of conductor and
axes of cable for 3 core cable
t_ins2mm = 1.2; %thickness of outer insulation [mm]
t_ins2 = t_ins2mm*10^(-3); %thickness of outer insulation [m]
d_ins2 = d_s+(2*t_ins2); %diameter of outer insulation [m]
d_cable = d_ins2;
if n == 1;
s_cab = s_con_axis(dd)*10^(-3); %separation between cable [m]
s_ax = d_cable+s_cab; %distance between cable axes [m]
else
s_ax = d_ins1; %1 core axes to another is the same for
2 or 3 cores, diameter of the insulation 1
end
%% MATERIAL
copper = material(cc)*1; %1=COPPER, else = ALUMINIUM
if copper == 1
%R20hub = 0.000259; %ohm/m, for 70mm2
%p = R20hub*70e-6; %resistivity of copper [Ohm.m]
%Rdc20 = p/Acon; %DC resistance of conductor at 20deg C per unit
length
Rdc20 = 0.000368; %for 50mm2
%Rdc20 = 0.00509; %for 4mm2
alpha20 = 3.93e-3; %constant mass temperature coefficiet at
20deg C per kelvin, provided by IEC60287-1-1
ur = 0.999994; %relative permeability
else
p = 2.8264*10^(-8); %resistivity of aluminium, from IEC60287-1-
1 [Ohm.m]
Rdc20 = p/Acon; %DC resistance of conductor at 20deg C per
unit length [Ohm/m]
alpha20 = 4.03e-3; %constant mass temperature coefficiet at
20deg C per kelvin, provided by IEC60287-1-1
ur = 1.000022; %relative permeability
end
Rdc_max = Rdc20*(1+alpha20*(T_end-20)); %dc resistance per unit length at
max operating temperature
p_shield = 1.38e-7; %Resistivity of tin plate copper braid [Ohm.m]
R_s = p_shield/Acon; %Resistance of shield
%% LOSSES
%Skin Effect and Skin Depth Calculation
68
ks = 1; %given in IEC60287-1, table 2. Stranded copper and aluminium both
ks and kp equal to 1
xs = sqrt(8*pi*f*power(10,-7)*ks/Rdc_max);
if 0 < xs <= 2.8
ys = (xs^4)/(192 + 0.8*(xs^4));
elseif 2.8 < xs <= 3.8
ys = -0.136 -0.0177*xs+0.0563*(xs^2);
else
ys = 0.354*xs - 0.733;
end
%Proximity Calculation -- Only for AC, thus only take yp for 3-core cable
or 3 single-core cables
xp = xs; %formula exactly the same but using kp instead of
ks. kp equals to 1, same with ks
ypfactor = 0.312*(dcon/s_ax)^2+1.18/(xp^4/(192+0.8*xp^4)+0.27);
yp = xp^4/(192+0.8*xp^4)*((dcon/s_ax)^2)*(ypfactor);
%AC Resistance
Rac_max = Rdc_max*(1+ys+yp);
ACtoDC = Rac_max/Rdc_max*100;
%Dielectric Losses Calculation - Not applicable
Wd = 0; %dielectric loss
%for single-core cable with sheaths bonded at both ends, only loss due to
%circulating current in the sheaths need to be considered. IEC
%Sheath and Screen Losses Factor Calculation
if typeofssloss == 1 %AC trefoil 3 Cables
edy_loss = 0; %lambda1"
X = 2*omega*10^(-7)*log(2*s_ax/d_s); %reactance per unit length
of cable
circ_loss = (R_s/Rac_max)*(1/(1+(R_s/X)^2));%lambda1'
elseif typeofssloss == 2 %AC Flat Formation
edy_loss = 0;
X = 2*omega*10^(-7)*log(2*s_ax/d_s); %reactance per unit length of
cable
Xm = 2*omega*10^(-7)*log(2);
P = X+Xm;
Q = X-(Xm/3);
helper1 = 0.75*P^2/(R_s^2+P^2);
helper2 = 0.25*Q^2/(R_s^2+Q^2);
helper3 = 2*R_s*P*Q*Xm/(sqrt(3)*(R_s^2+Q^2)*(R_s^2+P^2));
circ_loss = R_s/Rac_max*(helper1+helper2+helper3);
circ_loss2 = R_s/Rac_max*(helper1+helper2-helper3);
circ_loss3 = R_s/Rac_max*(Q^2/(R_s^2+Q^2));
else typeofssloss == 3; %AC - 3 cores 1 cable
if R_s <= 100*10^(-6);
helper4 = (R_s/omega*10^7)^2;
helper5 = (2*d_cc/d_s)^2*(1/(1+helper4));
helper6 = (2*d_cc/d_s)^4*(1/(1+4*helper4));
edy_loss = 3*R_s/Rac_max*(helper5+helper6);
circ_loss = 0;
else
edy_loss = 3.2*omega^2/(Rac_max*R_s)*(2*d_cc/d_s)^2*10^(-14);
circ_loss = 0;
end
end
lambda1 = circ_loss+edy_loss; %lambda1, loss factor for sheath and screen
69
lambda2 = 0; %idk lambda2
%% T1, T2, T3 Calculation
rho_155 = 4.31; %resistivity of RADOX 155
rho_elastomer = 4.1; %resistivity of RADOX Elastomer
rho_t1 = rho_155; %thermal resistivity of the inner insulation [K.m/W]
rho_i1 = rho_155; %thermal resistivity of the insulation, for 3 core
[K.m/W]
rho_f1 = rho_155; %thermal resistivity of the filler material [K.m/W]
Gt1perdc = t_ins1/dcon; %Geometry Factor
if TR1Factor == 1;
T1 = (rho_t1/(2*pi))*log(1+2*t_ins1/dcon);
elseif TR1Factor == 2;
if Gt1perdc <= 0.1;
G = 0.5; %taken from IEC60287-2-1, figure 2
elseif 0.1 < Gt1perdc <= 0.4
m = 2 %gradient area 1
G = m*(Gt1perdc-0.1)+0.5;
elseif 0.4 < Gt1perdc <= 0.7
m = 1.1667 %gradient area 2
G = m*(Gt1perdc-0.4)+1.1;
elseif 0.7 < Gt1perdc <= 1.2;
m = 0.70 %gradient area 3
G = m*(Gt1perdc-0.7)+1.45;
elseif 1.2 < Gt1perdc <= 1.8;
m = 0.5000 %gradient area 4
G = m*(Gt1perdc-1.2)+1.8;
elseif Gt1perdc > 1.8
m = 0.41667 %gradient area 5
G = m*(Gt1perdc-1.8)+2.1;
end
T1 = rho_t1*G/(2*pi)
elseif TR1Factor == 3;
if Gt1perdc <= 0.1;
G = 0.5; %taken from IEC60287-2-1, figure 3
elseif 0.1 < Gt1perdc <= 0.3
m = 3 %gradient area 1
G = m*(Gt1perdc-0.1)+0.5;
elseif 0.3 < Gt1perdc <= 0.7
m = 1.25 %gradient area 2
G = m*(Gt1perdc-0.3)+1.1;
elseif 0.7 < Gt1perdc <= 1.3;
m = 0.834 %gradient area 3
G = m*(Gt1perdc-0.7)+1.6;
elseif 1.3 < Gt1perdc <= 1.9;
m = 0.5000 %gradient area 4
G = m*(Gt1perdc-1.3)+2.1;
elseif Gt1perdc > 1.9
m = 0.4 %gradient area 5
G = m*(Gt1perdc-1.9)+2.4;
end
T1 = rho_i1*G/(2*pi)+(0.031*(rho_f1 - rho_i1)*exp(0.67*t_ins1/dcon));
end
%T2 Calculation
T2 = 0;
%T3 Calculation
70
rho_t3 = rho_elastomer; %thermal resistivity of outer insulation
T3 = rho_t3/(2*pi)*log(1+2*t_ins2/d_s);
%% T4 Calculation
if formationtype == 1;
Z_iec = 0.29; E_iec = 2.35; g_iec = 0.5;
elseif formationtype == 2;
Z_iec = 1.42; E_iec = 0.86; g_iec = 0.25;
elseif formationtype == 4
Z_iec = 0.75; E_iec = 2.8; g_iec = 0.3;
elseif formationtype == 5
Z_iec = 0.94; E_iec = 0.79; g_iec = 0.2;
elseif formationtype == 6
Z_iec = 0.62; E_iec = 1.95; g_iec = 0.25;
elseif formationtype == 7;
Z_iec = 1.61; E_iec = 0.42; g_iec = 0.2;
elseif formationtype == 9; %8 in the IEC
Z_iec = 1.31; E_iec = 2; g_iec = 0.2;
else %3, 8, 10
Z_iec = 1.69; E_iec = 0.63; g_iec = 0.25;
end
heatc = (Z_iec/d_cable^g_iec)+E_iec; %heat coefficient IEC
K_A = pi*d_cable*heatc*(T1/n+T2+T3); %neglect the AC losses
dThetas = 2 %initial number given, remember that dThetas always in
the power of 1/4
diff_dThetas = 1000 %random
iterasi = 0
while diff_dThetas > 0.001
dThetas_1 = power(dT/(1+K_A*dThetas),0.25)
diff_dThetas = dThetas_1 - dThetas
dThetas = dThetas_1
iterasi = iterasi + 1
end
T4 = 1/(pi*d_cable*heatc*(dThetas));
%% AMPACITY DC
%DC & AC show the same result in f = 0
huy = Wd*(0.5*T1+n*(T2+T3+T4))
I_DC_compare_end (ee) = sqrt(dT/((Rdc_max*T1)+(n*Rdc_max*(T2+T3+T4))));
I_AC_compare_end (ee) = sqrt((dT-
0)/(Rac_max*T1+n*Rac_max*(1+lambda1)*T2+n*Rac_max*(1+lambda1+lambda2)*(T3+T
4)));
%collecting per variation
I_T_end (ee) =
sqrt((dT)/(Rac_max*T1+n*Rac_max*(1+lambda1)*T2+n*Rac_max*(1+lambda1+lambda2
)*(T3+T4)));
I_CSA (aa) =
sqrt((dT)/(Rac_max*T1+n*Rac_max*(1+lambda1)*T2+n*Rac_max*(1+lambda1+lambda2
)*(T3+T4)));
I_T_amb (bb) =
sqrt((dT)/(Rac_max*T1+n*Rac_max*(1+lambda1)*T2+n*Rac_max*(1+lambda1+lambda2
)*(T3+T4)));
%material variation
if (cc) == 1;
I_CSA_cop = I_CSA;
I_T_amb_cop = I_T_amb;
71
I_T_end_cop = I_T_end;
else
I_CSA_al = I_CSA;
I_T_amb_al = I_T_amb;
I_T_end_al = I_T_end;
end
%I as function of Tambient, combined with T in conductor. Figure 5
%could be copper or aluminium
if (cc) == 1 %for copper
if (bb) == 1 %20 deg C
I_T_end20_cop = I_T_end
elseif (bb) == 2 %40 deg C
I_T_end40_cop = I_T_end
elseif (bb) == 3 %60 deg C
I_T_end60_cop = I_T_end
elseif (bb) == 4 %80 deg C
I_T_end80_cop = I_T_end
end
else
if (bb) == 1 %20 deg C
I_T_end20_al = I_T_end
elseif (bb) == 2 %40 deg C
I_T_end40_al = I_T_end
elseif (bb) == 3 %60 deg C
I_T_end60_al = I_T_end
elseif (bb) == 4 %80 deg C
I_T_end80_al = I_T_end
end
end
end
end
end
end
end
%% GRAPHICS
figure(1)
plot(A_con, I_CSA_cop, 'r-o',A_con,I_CSA_al,'b-*')
legend('copper','aluminium')
xlabel('Cross Section [mm2]')
ylabel('Cable Ampacity [A]')
title('Single-core Cable';'Ambient Temperature = 20 C'; ' Max Conductor
Temperature = 90 C')
grid on
figure(2)
plot(T_start, I_T_amb_cop,'r-o', T_start, I_T_amb_al, 'b-*')
legend('copper','aluminium')
xlabel('Ambient Temperature [deg C]')
ylabel('Cable Ampacity [A]')
title('Single-core Cable';'Conductor Cross Section Area = 70mm2'; ' Max
Conductor Temperature = 90 C')
grid on
figure(4)
plot(I_T_end_cop,T_con,'r-o', I_T_end_al,T_con,'b-*')
72
legend('copper','aluminium')
ylabel('Conductor Temperature [deg C]')
xlabel('Continuous Current Applied [A]')
title('Single-core Cable';'Cross Section Area = 70mm2'; 'Tamb = 20 degC')
grid on
%main, many plot
figure(5)
plot( I_T_end20_cop, T_con, 'g', I_T_end40_cop, T_con, 'b',
I_T_end60_cop, T_con, 'y', I_T_end80_cop, T_con, 'r', 'LineWidth',1.2)
ylabel('Conductor Temperature [deg C]')
xlabel('Continuous Current Applied [A]')
title('Single-core Cable';'Two Cables Touching, Vertical';'Cross Section
Area = 50 mm2')
hleg = legend('25','40', '60', '80');
htitle = get(hleg,'Title');
set(htitle,'String','Ambient Temperature [deg C]')
grid on
73
Short Circuit Calculation Code
%% SHORT CIRCUIT CAPABILITY
clear all
clc
Tscmax1 = 250;
T_01 = 100;
t_cl1 = [0.05:0.01:5];
A_con1 = [20 30 50 70]; %cross section [mm2]
for dd = 1:length(A_con1)
for cc = 1:length(t_cl1);
t_c = t_cl1(cc)*1;
A_con = A_con1(dd)*(1973.52524139); %convert the unit to per mil
Isc(cc) = A_con*sqrt(0.0297*log((Tscmax1+234)/(T_01+234))/t_c);
%CSA variation
if (dd) == 1 %20
ISC20 = Isc
elseif (dd) == 2 %30
ISC30 = Isc
elseif (dd) == 3 %50
ISC50 = Isc
elseif (dd) == 4 %70
ISC70 = Isc
end
end
end
figure(1)
plot( t_cl1, ISC20, 'r', t_cl1, ISC30, 'b', t_cl1, ISC50, 'k', t_cl1,
ISC70, 'y')
legend('CSA = 20','CSA = 30', 'CSA = 50', 'CSA = 70')
ylabel('Maximum Short Circuit Current[A]')
xlabel('clearance time [s]')
title('Short Circuit Withstand Capability')
grid on
74
Voltage Drop Calculation Code
%% AC VOLTAGE DROP CALCULATION
clear all
clc
long = [0:1:150];
A_con = 50; %cross section [mm2]
T_end = 120; %Temperature end variable in matlab [deg C]
f = 700;
pf = [1 0.85 0.7 0.55 0.4 0.1];
material = 1; %1=COPPER, 2 = ALUMINIUM
I_con = 200;
s_con_axis = [0]; %separation of cable [mm]
%% CONTROL Variable
n = 1; %number of conductor in a cable
%% for LOOP start
for aa = 1:length(pf);
for bb = 1:length(long);
%% GENERAL
Vbaseac = 650;
Vbasedc = 900;
omega = 2*pi*f;
costheta = pf(aa)*1;
degree = acosd(costheta);
sintheta = sind(degree);
leng = long(bb)*1;
%% GEOMETRY
Acon = A_con*10^(-6); %cross section [m2]
rcon = sqrt(Acon/pi); %radius of conductor [m]
dcon = 2*rcon; %diameter of conductor [m]
t_ins1mm = 2.1; %thickness of inner insulation [mm]
t_ins1 = t_ins1mm*10^(-3); %thickness of inner insulation [m]
d_ins1 = dcon+(2*t_ins1); %diameter of insulation [m]
t_smm = 0.5; %thickness of shield [mm]
t_s = t_smm*10^(-3); %thickness of shield [m]
if n == 1; %mean diameter of the screen [m]
d_s = d_ins1+(2*t_s);
elseif n == 2;
d_s = (2*d_ins1)+(2*t_s);
elseif n == 3; %use equilateral triangle
d_s = 2*((d_ins1/sqrt(3))+0.5*d_ins1) + (2*t_s);
end
d_cc = d_ins1/sqrt(3); %distance between axes of conductor and
axes of cable for 3 core cable
t_ins2mm = 1.2; %thickness of outer insulation [mm]
t_ins2 = t_ins2mm*10^(-3); %thickness of outer insulation [m]
d_ins2 = d_s+(2*t_ins2); %diameter of outer insulation [m]
d_cable = d_ins2;
if n == 1;
75
s_cab = s_con_axis*10^(-3); %separation between cable [m]
s_ax = d_cable+s_cab; %distance between cable axes [m]
else
s_ax = d_ins1; %1 core axes to another is the same for
2 or 3 cores, diameter of the insulation 1
end
%% MATERIAL
copper = material*1; %1=COPPER, else = ALUMINIUM
if copper == 1
R20hub = 0.000259; %ohm/m, for 70mm2
p = R20hub*70e-6; %resistivity of copper [Ohm.m]
Rdc20 = p/Acon; %DC resistance of conductor at 20deg C per
unit length [Ohm/m]
alpha20 = 3.93e-3; %constant mass temperature coefficiet at
20deg C per kelvin, provided by IEC60287-1-1
ur = 0.999994; %relative permeability
else
p = 2.8264*10^(-8); %resistivity of aluminium, from IEC60287-1-
1 [Ohm.m]
Rdc20 = p/Acon; %DC resistance of conductor at 20deg C per
unit length [Ohm/m]
alpha20 = 4.03e-3; %constant mass temperature coefficiet at
20deg C per kelvin, provided by IEC60287-1-1
ur = 1.000022; %relative permeability
end
Rdc_max = Rdc20*(1+alpha20*(T_end-20)); %dc resistance per unit length at
max operating temperature
R_s = 0.0037; %ohm/m. Shielding tin copper braid, from COROPLAST
%% LOSSES
%Skin Effect and Skin Depth Calculation
ks = 1; %given in IEC60287-1, table 2. Stranded copper and aluminium both
ks and kp equal to 1
xs = sqrt(8*pi*f*power(10,-7)*ks/Rdc_max);
if 0 < xs <= 2.8
ys = (xs^4)/(192 + 0.8*(xs^4));
elseif 2.8 < xs <= 3.8
ys = -0.136 -0.0177*xs+0.0563*(xs^2);
else
ys = 0.354*xs - 0.733;
end
%Proximity Calculation -- Only for AC, thus only take yp for 3-core cable
or 3 single-core cables
xp = xs; %formula exactly the same but using kp instead of
ks. kp equals to 1, same with ks
ypfactor = 0.312*(dcon/s_ax)^2+1.18/(xp^4/(192+0.8*xp^4)+0.27);
yp = xp^4/(192+0.8*xp^4)*((dcon/s_ax)^2)*(ypfactor);
%AC Resistance
Rac_max = Rdc_max*(1+ys+yp);
ACtoDC = Rac_max/Rdc_max*100;
X = 2*omega*10^(-7)*log(2*s_ax/d_s); %reactance per unit length of
cable
%% RESULT
76
%aa = pf variation
if aa == 1;
Vd_ac1 = I_con*sqrt(3)*leng*(Rac_max*costheta+X*sintheta); %AC Voltage
Drop
drop_ac1(bb) = Vd_ac1/Vbaseac*100;
elseif aa == 2;
Vd_ac85 = I_con*sqrt(3)*leng*(Rac_max*costheta+X*sintheta); %AC Voltage
Drop
drop_ac85 (bb)= Vd_ac85/Vbaseac*100;
elseif aa == 3;
Vd_ac7 = I_con*sqrt(3)*leng*(Rac_max*costheta+X*sintheta); %AC Voltage
Drop
drop_ac7(bb) = Vd_ac7/Vbaseac*100;
elseif aa == 4;
Vd_ac55 = I_con*sqrt(3)*leng*(Rac_max*costheta+X*sintheta); %AC Voltage
Drop
drop_ac55(bb) = Vd_ac55/Vbaseac*100;
elseif aa == 5;
Vd_ac4 = I_con*sqrt(3)*leng*(Rac_max*costheta+X*sintheta); %AC Voltage
Drop
drop_ac4(bb) = Vd_ac4/Vbaseac*100;
elseif aa == 6;
Vd_ac01 = I_con*sqrt(3)*leng*(Rac_max*costheta+X*sintheta); %AC Voltage
Drop
drop_ac01(bb) = Vd_ac01/Vbaseac*100;
end
end
end
%% GRAPH
figure(1)
plot(long, drop_ac1, 'r', long, drop_ac85, 'b',long, drop_ac7, 'k',long,
drop_ac55, 'g',long, drop_ac4, 'y',long, drop_ac01, 'm');
legend('pf 1','pf 0.85','pf 0.7','pf 0.55','pf 0.4','pf 0.1')
grid on
77
Bibliography
1. International Energy Agency, Global EV Outlook 2018 : Towards Cross-Modal Electrification.
2018: Paris. p. 141.
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