DESIGN AND OPTIMISATION OF THREE-PHASE SALIENT ROTOR...
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DESIGN AND OPTIMISATION OF THREE-PHASE
SALIENT ROTOR WOUND FIELD FLUX
SWITCHING MOTOR
FAISAL KHAN
UNIVERSITI TUN HUSSEIN ONN MALAYSIA
DESIGN AND OPTIMISATION OF THREE-PHASE SALIENT ROTOR WOUND
FIELD FLUX SWITCHING MOTOR
FAISAL KHAN
A thesis submitted in
fulfilment of the requirement for the award of the
Doctor of Philosophy in Electrical Engineering
Faculty of Electrical and Electronic Engineering
Universiti Tun Hussein Onn Malaysia
November 2016
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This dissertation is dedicated to my parents, my wife, my brother, and sisters, who
have always encouraged me with their love and prayers.
DEDICATION
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ACKNOWLEDGEMENT
I am very thankful to Almighty ALLAH for without His graces and blessings,
this study would not have been possible.
Since I started my PhD research work, several people and organisations have
been involved directly and indirectly with my project. They have loyally provided
me encouragement, motivation, moral, and financial support. Hereby, I express my
gratitude to them.
I would like to thank my supervisor, Assoc. Prof. Ir. Dr. Erwan Sulaiman, for
providing the opportunity to be one of his students. His guidance and support during
the entire study made it possible for me to write this thesis. I am continually amazed
by his discipline, research, and scientific skills.
This PhD project has been made possible with the financial support from the
ORICC, Universiti Tun Hussein Onn Malaysia, and Ministry of Higher Education
(MOHE), Malaysia. I would like to record my gratitude to the staffs from ORICC
who have been involved in my project. I would like to thank COMSATS Institute of
Information Technology, Abbottabad Campus for granting me study leave for PhD
studies.
My sincere thanks go to Mr. Md Zarafi Ahmad for his convincing
explanations and important contributions. I also want to thank Mr. Mohd Fairoz
Omar and Mr. Gadafi M. Romalan for sharing practical and theoretical knowledge.
Furthermore, I wish to express my sincere gratitude to my family for their
moral support and prayers. I would like to thank my grandfather, Mr. Haji Aslam
Khan Malik and father, Mr. Nifaz Ali for their prayers and support, and also to my
mother, the one who had made me successful with her caring and gentle love. I
would also like to thank to my wife for her support, endless encouragement, prayers,
and love. She had spent lots of time taking care of our lovely daughter Burooj during
my study period. To my brother Mr. Shah Saud, I would like to say thanks for
supporting my family throughout my PhD studies.
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ABSTRACT
Permanent magnet-free wound field flux switching machine (WFFSM) with a
segmented rotor and non-overlapping windings is an attractive alternative for driving
high torque density applications due to their low cost, high efficiency, high average
torque and power. However, a rotor with segments makes the motor less robust and
difficult to be assembled, while WFFSM with salient rotor and overlapping windings
inherit high copper losses and less efficiency due to their long end-windings. This
thesis deals with a novel structure of WFFSM employing a salient rotor with non-
overlapping field and armature windings on the stator and a presentation of an
unexcited rotor. The non-overlapping winding arrangement on the stator consumes
less copper material, thus improves the efficiency. Moreover, the salient rotor
structure with high mechanical strength is suitable for high-speed operation. The
design restrictions and specifications of the proposed motor are keep similar as
WFFSM with a segmented rotor. The JMAG-Designer ver.14.1 was used to verify
the motor’s operating principle and performance characteristics. Three-phase
configurations of WFFSM with non-overlap windings and salient rotor were studied,
from the design features to performance analysis. For the three-phase operation, 11
topologies were feasible when employing a 12-tooth and 24-tooth stator. The
subsequent optimisation work carried out using deterministic optimisation approach
and Genetic Algorithm (GA) method to achieve the target average torque of 25.8 Nm
and power of 6.49 kW. Designed and analysed by 2D and 3D finite element analysis
(FEA), the optimised 12S-10P configuration had achieved high torque and power of
4.6% and 4.8% respectively, as compared to 12S-8P WFFSM with segmental rotor
and non-overlapping windings. Moreover, the torque and power of the optimised
design were also greater than 12S-8P WFFSM with salient rotor and overlapping
windings. The 12S-14P topology had produced high average torque and power at low
armature and field currents compared with all designs.
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ABSTRAK
Mesin fluks beralih medan-belitan tanpa magnet kekal (WFFSM) dengan pemutar
bersegmen dan belitan tidak bertindih adalah alternatif yang menarik terhadap
aplikasi yang memerlukan ketumpatan tork yang tinggi. Ini disebabkan oleh kos
yang rendah, kecekapan, tork dan kuasa purata yang tinggi. Walau bagaimanapun,
pemutar bersegmen menjadikan motor kurang teguh serta sukar untuk dipasang,
manakala, WFFSM dengan pemutar menonjol dan belitan bertindih menyebabkan
kerugian pada penggunaan tembaga yang tinggi dan kecekapan yang kurang akibat
daripada penghujung belitan yang panjang. Tesis ini berkaitan struktur baru WFFSM
menggunakan pemutar menonjol yang mempunyai medan dan angker tanpa belitan
bertindih pada pemegun dan pemutar yang tidak teruja. Susunan penggulungan tidak
bertindih pada pemegun yang menggunakan kurang bahan tembaga, sekaligus
mampu meningkatkan kecekapan. Selain itu, struktur pemutar menonjol dengan
kekuatan mekanikal yang tinggi adalah sesuai untuk operasi mesin pada kelajuan
tinggi. Had rekabentuk dan spesifikasi motor yang dicadangkan adalah masih sama
seperti WFFSM dengan pemutar bersegmen. Perisisan JMAG-Designer versi 14.1
telah digunakan untuk mengesahkan prinsip operasi dan prestasi motor. Konfigurasi
tiga fasa WFFSM dengan belitan tidak bertindih dan pemutar menonjol telah dikaji,
bermula dengan ciri-ciri rekabentuk sehingga analisis prestasi. Bagi operasi tiga fasa,
11 topologi telah dilaksanakan apabila menggunakan 12-gigi dan 24-gigi pemegun.
Kerja-kerja pengoptimuman berikutnya dijalankan menggunakan pendekatan
pengoptimuman berketentuan dan kaedah algoritma genetik (GA) untuk mencapai
sasaran tork purata 25.8 Nm dan kuasa 6.49 kW. Setelah mesin direka dan dianalisis
menggunakan kaedah 2D dan 3D analisis unsur terhingga (FEA), konfigurasi 12S-
10P yang telah dioptimumkan telah mencapai tork yang tinggi dan kuasa sebanyak
4.6% dan 4.8% masing-masing, berbanding 12S-8P WFFSM dengan pemutar
bersegmen dan belitan tidak bertindih. Selain itu, tork dan kuasa rekabentuk yang
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dioptimumkan juga lebih tinggi daripada 12S-8P WFFSM dengan rotor menonjol
dan belitan bertindih. Topologi 12S-14P telah menghasilkan tork purata dan kuasa
yang tinggi pada arus angker dan arus medan yang rendah berbanding dengan
keseluruhan rekabentuk motor.
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TABLE OF CONTENTS
DECLARATION ii
DEDICATION iii
ACKNOWLEDGEMENT iv
ABSTRACT v
ABSTRAK vi
TABLE OF CONTENTS viii
LIST OF TABLES xiii
LIST OF FIGURES xiv
LIST OF SYMBOLS AND ABBREVIATIONS xviii
LIST OF APPENDICES xx
LIST OF PUBLICATIONS xxi
LIST OF AWARDS xxiv
CHAPTER 1 INTRODUCTION 1
1.1 Research Background 1
1.2 Problem Statement 3
1.3 Objectives of the Study 4
1.4 Scope 4
1.5 Motivations for Research 5
1.6 Contribution to Knowledge 6
1.7 Thesis Organisation 6
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CHAPTER 2 OVERVIEW OF FLUX SWITCHING MOTORS 9
2.1 Introduction 9
2.2 Operation and classification of the Flux Switching
Machine 10
2.3 Permanent Magnet Flux Switching Motor (PMFSM) 12
2.3.1 Various Configurations of PMFSMs 12
2.3.2 Modelling Techniques of PMFSMs 13
2.4 Hybrid Excitation Flux Switching Motor (HEFSM) 15
2.5 Field Excitation Flux Switching Motor (FEFSM) 17
2.5.1 Structure review of FEFSM 17
2.5.2 Design restrictions and specifications for FEFSMs 20
2.5.3 Flux linkages of various FEFSMs 21
2.5.4 Cogging torque of FEFSMs 22
2.5.5 Average torque and efficiency 23
2.5.6 Analytical comparison of FEFSMs 26
2.6 Summary 29
CHAPTER 3 DESIGN METHODOLOGY 30
3.1 Introduction to JMAG-Designer software 30
3.2 Project methodology of proposed SalRoN WFFSM 30
3.2.1 Design process and coil arrangement test 31
3.2.2 Performance analysis of SalRoN WFFSM 36
3.2.2.1 Rotor mechanical properties 38
3.2.2.2 Torque density/ Power density 38
3.2.3 Optimisation of SalRoN WFFSM 39
3.3 Summary 41
CHAPTER 4 CHARACTERISTICS INVESTIGATION OF
THE PROPOSED SALRON WFFSM 42
4.1 Various rotor pole topologies comparison of three-phase
12 slots SalRoN WFFSM on the basis of FEA 42
4.1.1 Coil test analysis and operating principle of
SalRoN WFFSM 43
4.1.2 Development of mathematical model and
equivalent circuit of SalRoN WFFSM 45
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4.1.3 Cogging torque 49
4.1.4 Induced EMF at open circuit condition 50
4.1.5 Effect of rotor pole width variation on
12S-8P SalRoN WFFSM 51
4.1.6 Torque versus Ja characteristics at various Je 52
4.1.7 Torque and power vs. speed characteristics of
12S-8P and 12S-10P SalRoN WFFSM 55
4.2 Various rotor pole topologies comparison of three-phase
24 slots WFFSM on the basis of FEA 56
4.2.1 Coil test analysis 56
4.2.2 Cogging torque 57
4.2.3 Induced EMF at open circuit condition 58
4.2.4 Torque versus Ja characteristics at various Je
for 24 slots topologies 59
4.2.5 Torque and power versus speed characteristics
of 24S-10P and 24S-14P SalRoN WFFSM 59
4.3 Other performances of SalRoN WFFSM 60
4.4 Performance comparison of SalRoN WFFSMs with
existing WFFSMs 64
4.4.1 Comparison of flux linkage 64
4.4.2 Comparison of cogging torque and average
torque 65
4.4.3 Torque and power versus speed characteristics
of 12S-8P SegRoN and SalRO WFFSMs 67
4.4.4 Efficiency analysis of 12S-8P SegRoN and
SalRO WFFSMs 68
4.5 Summary 69
CHAPTER 5 DESIGN OPTIMISATION 70
5.1 Design Optimisation of 24S-10P, 12S-8P, 12S-10P,
and 12S-14P SalRoN WFFSMs 70
5.1.1 Comparison between GA and deterministic
optimisation methods for cycle 1 73
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5.1.2 Influence of design parameters on flux
distribution and flux linkages 76
5.1.3 Cogging torque and induced EMF at
open circuit condition 77
5.1.4 Torque and power comparison at maximum
Je and Ja 81
5.1.5 Transformation of trapezoidal slots of 12S-10P
SalRoN WFFSM to rectangular slots 82
5.1.6 Design optimisation of 12S-10P and 12S-14P
SalRoN WFFSMs with rectangular slots 82
5.1.6.1 Performance analysis comparison of optimised
design of 12S-10P and 12S-14P SalRoN
WFFSMs 88
5.1.6.2 Design techniques for cogging torque
reduction of 12S-10P and 12S-14P 92
5.1.7 Torque and power versus speed characteristics
of optimised design of SalRoN WFFSMs 95
5.1.8 Torque and power densities of optimised
SalRoN WFFSMs 96
5.1.9 Losses and efficiencies of optimised SalRoN
WFFSMs 97
5.1.10 Performances comparison of optimised
SalRoN WFFSMs 98
5.2 Comparison of optimised SalRoN WFFSMs with
same and different FEC polarities 99
5.2.1 2D and 3D FEA performance comparison
of SalRoN WFFSMs 101
5.3 Cost analysis comparison of SalRoN WFFSM with
brushless machines 103
5.4 Practical applications of proposed SalRoN WFFSMs 104
5.5 Summary 105
CHAPTER 6 CONCLUSION AND FUTURE WORKS 106
6.1 Conclusion 106
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6.2 Future works 107
REFERENCES 109
APPENDIX 121
VITA 131
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LIST OF TABLES
2.1 FEFSMs Comparison 21
3.1 Design parameters of SalRoN WFFSM 36
4.1 Torque and power densities 63
4.2 Losses and efficiencies of the 12S-8P SegRoN
and SalRO WFFSMs 68
5.1 Design parameters for improved designs 73
5.2 Design restrictions and specifications of 12S-10P
SalRoN WFFSM 83
5.3 Initial and optimised design parameters 87
5.4 Comparison of torque and power densities of
optimised designs 96
5.5 Losses and efficiencies at various operating points 97
5.6 Performances comparison of optimised SalRoN
WFFSMs 98
5.7 Main parameters of SalRoN WFFSMs 99
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LIST OF FIGURES
1.1 Three-phase FEFSM 3
2.1 A flux switching inductor alternator 10
2.2 Basic operation principle with constant field winding
excitation and single-phase armature current 11
2.3 Classifications of FSM 12
2.4 Topologies of PMFSMs 14
2.5 HEFSM examples 16
2.6 Single-phase FEFSMs 18
2.7 Three-phase FEFSM 20
2.8 Flux distribution 22
2.9 Cogging torque of three-phase FEFSM 23
2.10 Average torque-current characteristics of FEFSMs 25
2.11 Total efficiency of FEFSM with segmental rotor 25
3.1 General work flow of project implementation 31
3.2 Work flow to design the SalRoN WFFSM and
investigate the coil arrangement test 32
3.3 Three-phase SalRoN WFFSM topologies have 12slots
and different rotor pole numbers 34
3.4 Three-phase SalRoN WFFSM topologies have
24slots and different rotor pole numbers 35
3.5 Performance analysis based on FEA 37
3.6 Estimated coil end volume of the SalRoN WFFSM 39
3.7 Deterministic optimisation procedure 40
3.8 Optimisation procedure using GA 40
4.1 Flux linkage of 12S-10P WFFSM in terms of U, V,
and W 44
4.2 U-phase flux linkage of 12 Slot WFFSMs SalRoN 44
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4.3 Principle of operation of WFFSM 44
4.4 Equivalent circuit of SalRoN WFFSM 487
4.5 Equivalent circuit of a SalRoN WFFSM 48
4.6 Cogging torque of 12 slot WFFSMs 49
4.7 Induced Voltage at 500 rpm 50
4.8 Flux linkage and cogging torque effect with variation
of rotor pole width 51
4.9 Harmonic magnitude with various rotor pole widths 52
4.10 Torque vs. Ja 53
4.11 Flux distribution at Je of 5 A/mm2 54
4.12 Torque and power versus speed characteristics of
12S-8P and 12S-10P SalRoN WFFSMs 55
4.13 Flux linkage of 24S-10P WFFSM topology in terms
of U, V, and W 57
4.14 Flux linkage in U-phase of 24 Slot WFFSMs 57
4.15 Cogging torque of 24 slots WFFSMs 58
4.16 Induced Voltage at 500 rpm 58
4.17 Torque vs. Ja at various Je of 24slot-10Pole 60
4.18 Torque and power vs. speed characteristics 60
4.19 Rotor stress analaysis at 500 rev/min 61
4.20 Mechanical stress versus speed 61
4.21 Motor losses and efficiency for operating shown
in Figure 4.12 63
4.22 Iron losses and copper losses at various points 63
4.23 12S-8P WFFSM 64
4.24 Flux distribution 65
4.25 Flux linkage of WFFSM at maximum Je 65
4.26 Cogging torque of WFFSM 66
4.27 Average torque of WFFSM at maximum Je 66
4.28 Torque and Power versus speed characteristics 67
5.1 Design parameters of SalRoN WFFSM 71
5.2 Effect of various motor parameters on average torque 72
5.3 Optimisation cycles of 12S-8P SalRoN WFFSM 73
5.4 Improved design of SalRoN WFFSMs 74
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5.5 Average torque versus rotor pole width based on
deterministic optimisation method 76
5.6 Average torque versus design variables based on
GA method 76
5.7 Effect of rotor pole width, R2 78
5.8 Flux distributions of 12S-8P 78
5.9 Flux distributions of 12S-10P 78
5.10 U-phase flux linkages of 24S-10P, 12S-8P and
12S-10P SalRoN WFFSMs 79
5.11 Comparison of cogging torque 79
5.12 Comparison of induced emf of SalRoN WFFSM 80
5.13 Comparison of torque and power of SalRoN
WFFSMs at maximum Jeof 30 A/mm2 and various Ja 81
5.14 12S-10P SalRoN WFFSM with rectangular slots 83
5.15 Design parameters of 12S-10P SalRoN WFFSM
with rectangular slots 84
5.16 Optimisation cycles to achieve better torque and
power characteristics 85
5.17 Torque and power versus number of turns 85
5.18 Optimised design of 12S-10P SalRoN WFFSM 87
5.19 Optimised design of 12S-14P SalRoN WFFSM 88
5.20 Average torque versus variable rotor pole width 88
5.21 Flux linkages comparison of optimized design of
12S-10P and 12-14P SalRoN WFFSMs 89
5.22 Cogging torque comparison 89
5.23 Torque versus Ja at various Je for optimized designs
of SalRoN WFFSM 90
5.24 Flux distribution of optimised design of 12S-14P
at Je of 5 A/mm2 and Ja of 15 Arms/mm2 91
5.25 Cogging torque reduction techniques 93
5.26 Comparison of various cogging torque reduction
schemes 94
5.27 Maximum and minimum value of cogging torque
for different schemes 94
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5.28 Torque versus speed characteristics of optimised
designs 95
5.29 Power versus speed characteristics of optimised
designs 95
5.30 12S-10P SalRoN WFFSM with identical polarity
of FECs 99
5.31 Torque versus various armature currents at field
current of 20 A 100
5.32 3D model of 12S-10P SalRoN WFFSM 101
5.33 Flux distribution of 12S-10P SalRoN WFFSM 102
5.34 Torque-armature current curves, Ie=20 A 103
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LIST OF SYMBOLS AND ABBREVIATIONS
- Efficiency
- Flux
exc - Flux linkage due to field excitation
- Electrical angular position of rotor
r - Rotational speed
- Copper resistivity
cog - Electrical angle of rotation for each period of cogging
torque
f - Filling factor
B - Magnetic flux density
F - Magnetomotive force
ef - Electrical frequency
mf - Mechanical rotation frequency
ai - Armature current
di - d-axis current
qi - q-axis current
fi - Field current
aJ - Armature current density
eJ - Field current density
k - Natural number
- Stack length
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N - Number of turns
pN - Number of periods
rN - Number of rotor poles
sN - Number of stator slots
cP - Copper loss
iP - Iron loss
mechP - Mechanical power
q - Number of phases
UR - Armature winding resistance per phase
- Reluctance
aS - Slot area
TL - Load torque
CAD - Computer Aided Design
CNC - Computer Numerical Control
HE - Hybrid Excitation
EV - Electric Vehicle
FSM - Flux Switching Motor
FE - Field Excitation
FEC - Field Excitation Coil
FEA - Finite Element Analysis
GA - Genetic Algorithm
HEV - Hybrid Electric Vehicle
IPMSM - Interior Permanent Magnet Synchronous Motor
MEC - Magnetic Equivalent Circuit
SalRoN - Salient Rotor and Non-overlapping windings
SalRO - Salient Rotor and Overlapping windings
SegRoN - Segmental Rotor and Non-overlapping windings
WFFSM - Wound Field Flux Switching Machine
WFSM - Wound Field Synchronous Machine
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LIST OF APPENDICES
APPENDIX TITLE PAGE
A. Conversion of U, V and W three-phase system
into d- and q-axis using Park’s transformation 121
B. Optimal values of design variables based on
Genetic Algorithm Method 123
C. Structure development of 12S-14P SalRoN WFFSM 125
D. Technical Drawing of 12S-14P SalRoN WFFSM 126
E. Gantt chart research activities 130
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LIST OF PUBLICATIONS
Journals:
(i) Faisal Khan, Erwan Sulaiman, Md. Zarafi Ahmad, “Review of Switched Flux
Wound-Field Machines Technology,” IETE Technical review, accepted,
DOI:10.1080/02564602.2016.1190304, 2016. (ISI, Scopus, Q2, IF: 1.30)
(ii) Faisal Khan, Erwan Sulaiman, Md Zarafi Ahmad, “A novel wound field flux
switching motor with non-overlapping windings and salient rotor,” Turkish
Journal of Electrical Engineering and Computer Science, accepted, DOI:
10.3906/elk-1507-80, 2016. (ISI, Scopus, Q2, IF: 0.507)
(iii) Faisal Khan, Erwan Sulaiman, Md Zarafi Ahmad, “Design and Analysis of
Wound Field Three-Phase Flux Switching Machine with Non-overlap
Winding and Salient Rotor,” International Journal of Electrical Engineering
and Informatics, vol.7, no. 2, pp. 323-333, 2015. (Scopus, Q3)
(iv) Faisal Khan, Erwan Sulaiman, Md Zarafi Ahmad, Zhafir Aizat, “Design
Refinement and Performance Analysis of 12Slot-10Pole Wound Field Salient
Rotor Switched-Flux Machine for Hybrid Electric Vehicles,” Journal of
Applied Science and Agriculture, vol. 9, no. 18, pp. 148-155, 2014. (ISI)
(v) Faisal Khan, Erwan Sulaiman, Md Zarafi Ahmad, Zhafir Aizat Husin, “Low
Cost and Robust Rotor Three-Phase Wound-Field Switched-Flux Machines
for HEV Applications,” APRN Journal of Engineering and Applied Sciences,
vol.10, no. 19, pp. 8858-8865, 2015. (Scopus, Q3)
(vi) Faisal Khan, Erwan Sulaiman, Md Zarafi Ahmad, “Performance comparison
of 24slot-10pole and 12slot-8pole wound field three-phase switched-flux
machine,” International Journal of Energy and Power Engineering Research,
vol. 2, pp. 17-21, 2014. (Non-indexed)
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(vii) Faisal Khan, Erwan Sulaiman, Mohd Fairoz Omar, “Flux Linkage Analysis
and Cogging Torque Reduction Techniques for Field-Excited Flux Switching
Machines,” Journal Technology, In press, 2016. (Scopus)
(viii)
(ix)
Faisal Khan, Erwan Sulaiman, Md Zarafi Ahmad and Zhafir Aizat,
“Parameter Sensitivity Study for Optimization of 12Slot-8Pole Three-Phase
Wound Field Switched-Flux Machine,” Journal- Applied Mechanics and
Materials, vol. 695, pp. 765-769, 2014.(Scopus)
Faisal Khan, Erwan Sulaiman, Zhafir Aizat Husin, Mubin Aizat Mazlan,
“Deterministic Optimization of Single Phase 8S-4P Field Excitation Flux
Switching Motor for Hybrid Electric Vehicle,”APRN Journal of Engineering
and Applied Sciences, vol. 11, no. 8, pp. 5084-5088, April 2016. (Scopus)
Proceedings:
(i) Faisal Khan, Erwan Sulaiman, Md Zarafi Ahmad, “Coil Test Analysis of
Wound-Field Three-Phase Flux Switching Machine with Non-overlap
Winding and Salient Rotor,” IEEE 8th International Power Engineering and
Optimization Conference, pp. 243-247, Langkawi, Malaysia, 24-25 March,
2014.
(ii) Faisal Khan, Erwan Sulaiman, Md Zarafi Ahmad, Zhafir Aizat Husin,
Mohamed Mubin Aizat Mazlan “Topologies for Three-Phase Wound-Field
Salient Rotor Switched-Flux Machines for HEV Applications,” International
Conference on Mathematics, Engineering & Industrial Applications, AIP
Publishing, vol. 1660, pp. 070097, Penang, Malaysia, 2015.
(iii) Faisal Khan, Erwan Sulaiman, Mohd Fairoz Omar, “Design and
Characteristics Investigations of 12Slot-8Pole and 12Slot-10Pole Wound
Field Three-Phase Switched-Flux Machines,” IET International Conference
on Clean Energy and Technology, pp. 1-5, Kuching, Malaysia, 24-26
November, 2014.
(iv) Faisal Khan, Erwan Sulaiman, Md Zarafi Ahmad, Hassan Ali, “Design
Refinement and Performance Analysis of 12Slot-8Pole Wound Field Salient
Rotor Switched-Flux Machine for Hybrid Electric Vehicles,” IEEE
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International conference on Frontier of Information Technology, pp. 197-201,
Islamabad, Pakistan, 17-19 December, 2014.
(v) Faisal Khan, Erwan Sulaiman, Md. Zarafi Ahmad, Zhafir Aizat Husin,
“Comparative study of 24Slot-10Pole and 24Slot-14Pole Wound filed
switched flux machine,” 8th Malaysian Technical Universities Conference on
Engineering & Technology, Melaka, Malaysia, 10-11 November, 2014.
(vi) Erwan Sulaiman, Faisal Khan, Md Zarafi Ahmad, Mahyuzie Jenal,
“Investigation of field excitation switched flux motor with segmental rotor,”
IEEE Conference on Clean Energy and Technology, pp.317-322, Langkawi,
Malaysia, 18-20 November, 2013.
(vii) Faisal khan, Erwan Sulaiman, “Design Optimization and Efficiency Analysis
of 12Slot-10Pole Wound Field Flux Switching Machine,” IEEE Magnetics
Conference, pp.1, Beijing, China, 11-15 May, 2015.
(viii) Faisal khan, Erwan Sulaiman, “Performance comparison of wound field Flux
switching machine,” IEEE Conference on Energy Conversion, pp. 310-314,
Johor Bahru, Malaysia, 19-20 October, 2015.
(ix) Faisal Khan, Erwan Sulaiman, Mohd Fairoz Omar, Mahyuzie Jenal, “3D FEA
based Performance of Wound Field Flux Switching Machine using JMAG,”
IEEE Student conference on Research and Development, pp. 362-366, 13-14
December, Kuala Lumpur, Malaysia, 2015.
(x) Erwan Sulaiman, Fasial Khan, Md Fairoz Omar, Gadafi M. Romalan,
Mahyuzie Jenal, “Optimal Design of Wound-Field Flux Switching Machines
for an All-Electric boat,” IEEE International Conference on Electrical
Machines, pp. 2464-2470, 4-7 September, Lausanne, Switzerland, 2016.
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LIST OF AWARDS
(i) Gold Medal in Seoul International Invention Fair, South Korea, [SIIF 2014]:
Erwan Sulaiman, Faisal Khan, Zhafir Aizat, Mubin Aizat, Sharifah Binti
Saon, “Field Excitation Flux Switching Motor”.
(ii) Silver Medal at Malaysia Technology Expo, Kuala Lumpur, [MTE 2014]:
Erwan Sulaiman, Faisal Khan, Zarafi Ahmad, Zhafir Aizat “12Slot-10Pole
Field Excitation Flux Switching Motor for Hybrid Electric Vehicles”.
(iii) Bronze Medal at Research & Innovation Festival, UTHM, [R & I 2013]:
Erwan Sulaiman, Faisal Khan, Zarafi Ahmad, Zhafir Aizat “Field Excitation
Flux Switching Motor for Hybrid Electric Vehicles”.
(iv) Silver Medal at Malaysia Technology Expo, Kuala Lumpur, [MTE 2015]:
Erwan Sulaiman, Mohd. Fairoz Omar, Faisal Khan, Hassan Ali Soomro,
Kamaluddin Hassan, “LoCo FEFS motor”.
(v) Copyright No. LY2015000027, Erwan Sulaiman, Faisal Khan “Wound Field
three-phase Flux Switching Motor with Non-overlap Winding and Salient
Rotor for Hybrid Electric Vehicles”.
(vi) Industrial Design No. 14-01422-0101, Erwan Sulaiman, Faisal Khan
“12Slot-10pole Wound Field three-phase Flux Switching Motor with Non-
overlap Winding and Salient Rotor for Hybrid Electric Vehicle”.
(vii) FRGS MOE Grant Vot. 1508, “Characteristic investigations of a New Field
Excitation Flux Switching Machine using Finite Element Analysis for Electric
Vehicles”.
(viii) Participated in 3 minutes PhD thesis competition, 2015 at national level held
at Kuala Lumpur, organised by UTM.
(ix) Patent File No. PI2016000833, Erwan Sulaiman, Faisal Khan, “Salient Rotor
Non-Overlapping Wound Field Flux Switching Motor”
(x) 3rd Prize in postgraduate poster competition, 2015 at UTHM.
CHAPTER 1
INTRODUCTION
1.1 Research Background
Nowadays, a majority of industrial and domestic applications require more compact,
more efficient, robust, light weight, and low-cost electric motors. As electric motors
are the core of both industrial and domestic appliances, there is a pressing need for
researchers to develop advanced electric motors. Latest research has made them
literally invisible, installed within thousands of everyday products. They can be
found in hybrid electric vehicles, fan, washing machine, air conditioners, vacuum
cleaner, aerospace application, and rigid disc drives [1]. There are several classes of
electric motors with standardised dimensions and characteristics. The development
of the flux switching motor (FSM) [2], a new class of brushless motor is as recent as
just over a decade ago. All the excitation sources of FSMs are located on the stator,
providing simpler cooling options, while the rotor consists of only a single piece
iron, neither magnet nor windings. FSMs are considered to be the most promising
electric motor with high efficiency, easy thermal management, robust rotor structure,
light weight, and cost-competitive. In addition, FSMs have been effectively applied
to domestic and industrial applications [3-6].
FSM is a combination of a switched reluctance motor and an inductor
alternator [7-8]. FSM can be categorised into three groups based on the method of
excitation to stator: (1) Permanent Magnet (PMFSM), (2) Field Excitation (FEFSM),
and (3) Hybrid Excitation (HEFSM). PM and field excitation coil (FEC) are the main
sources of flux in PMFSM and FEFSM respectively while for HEFSM, both PM and
FEC generate the flux [9-11]. Recently, the research work on PMFSM is dominated
2
by employing PM for primary excitation because of its high torque density, fault
tolerance, and high efficiency [12]. However, with the growing demand of PM for
electric motors, the annual consumption of rare-earth magnet has increased
accordingly. This causes the prices of Neodymium (Nd) and Dysprosium (Dy) – an
essential additive to provide the rare-earth magnet with high coercivity to rise
markedly. Together, they raised serious concerns about soaring cost, security issues,
and supply shortages. Hence, continuous research effort to develop electric motors
with high power density and robust rotor structure without relying on rare-earth
magnet is of the utmost importance [13]. It is desirable to completely replace the PM
with FEC or diminish the usage of PM. In order to compete with existing PMFSM,
some FEFSMs have been proposed for low cost and high-speed applications. The
FEFSM has advantages of low cost, simple construction, magnet-less machine, and
variable flux control capabilities suitable for various performances. The power
density of FEFSM is higher, as the working temperature of FEFSM will not be
limited by the working temperature of PMFSM [14-16]. The type of FSM that would
be discussed within the context of this thesis is the FEFSM.
The three-phase FEFSM was simply designed by replacing the PM of 24Slot-
10Pole PMFSM with FEC. However, the total flux generation was limited due to
isolation of DC FEC and thus reducing the performances [14]. Moreover, the
configuration of non-overlapping winding, instead of overlapping winding is
preferred for machine design because of its advantages of short end windings and
simple structure. If the slot pitch was close to the pole pitch, as in the case of similar
numbers of slots and poles, then copper losses were reduced and high torque was
produced in a non-overlapping winding, as discussed in [17-19]. To improve the
drawbacks of FEFSM, 12S-8P FEFSM with segmental rotor was designed and
experimentally tested [20]. Concentrated winding arrangement was used in this
design, which gave shorter end windings of DC FEC and armature coil when
compared with tooth rotor structure with distributed windings. This design had
significant gains over other designs, as it utilised less conductor materials, thus
improving the overall efficiency because of the reduction of copper loss. Examples
of FEFSMs with single and dual polarity FEC were discussed in [21] and [5]. The
advantages of FEFSM with single polarity FEC are low copper loss due to less
volume of FEC, less leakage flux when compared with dual FEC windings. The
field-weakening capability of FEFSM was improved using toroidal DC FEC [22].
3
1.2 Problem Statement
FEFSM was developed to overcome the drawbacks of rare earth materials used in
PMFSM [13], demagnetisation problem [23], uncontrollable flux and less robust
rotor owing to interior PM [24]. Various FEFSM structures are shown in Figure 1.1.
There are certain problems in FEFSM such as segmental rotor that made the rotor
less robust and cannot be used for high-speed application, as illustrated in
Figure 1.1(a) [15], and overlapping armature and field windings that raised the
copper losses in these machines [5], as shown in Figure 1.1(b). The segmented rotor
FEFSM design has noteworthy gain over other designs as it consume less conductor
(a) (b)
(c) (d)
Figure 1.1: Three-phase FEFSM, (a) 12S-8P FEFSM with segmental rotor, (b) 24S-10P FEFSM with dual FEC, (c) 24S-10P FEFSM with single FEC,
(d) 12S-14P FEFSM with toroidal DC winding
A2
C2 B2
A1
C1 B1
FEC-2
FEC-1
FEC-2
FEC-1
FEC-2
FEC-1
FEC-1
FEC-2 A1
B1
C1
A2
B2 C2 A3
B3
C3
A4 B4 C4
A1
B1 C1
A2
B2
C2
A3 B3
C3
A1
B1
A2
B2 C2
A3
B3
C3
A4 B4 C4
FEC FEC
FEC
FEC FEC
FEC
FEC
FEC
FEC
FEC FEC
FEC
FEC
C1
4
materials, accordingly enhanced the overall efficiency due to reduction of copper
loss. To deal with the problems, continuous research and development on electric
machines with no PM, stable current, high synchronous speed and high efficiency
would be very important.
FEFSM with single polarity FEC was discussed in [21], as shown in
Figure 1.1(c). FEFSM with single polarity FEC has advantages of less copper loss
when compared with dual FEC windings but the torque generation is limited. The
field-weakening capability of FEFSM is improved using toroidal dc field winding, as
shown in Figure 1.1(d). The proposed machine had limited torque generation,
because the field flux produced by DC field conductors close to the outer surface of
the stator went through the outside of the stator instead of the rotor, as well as high
copper losses owing to overlapped armature and field windings.
1.3 Objectives of the Study
The main objective of this research is to develop a novel structure of salient rotor and
non-overlapping windings (SalRoN) wound field flux switching motor (WFFSM)
for high-speed applications. In achieving the main objective, there are some specific
objectives that have to be fulfilled, which are:
(i) To design a novel SalRoN WFFSM and investigate its operating principle.
(ii) To investigate and analyse the significance of the new machine; the torque
speed characteristics, mechanical stress of the rotor, torque density, power
density, iron losses, copper losses of windings, and efficiency should be
examined.
(iii) To optimise the SalRoN WFFSM for better average torque, output power,
efficiency and torque-speed characteristics.
1.4 Scope
Commercial FEA package, JMAG-Designer ver.14.1, released by Japan Research
Institute (JRI), was used as 2D-FEA solver for this design. 12 stator-slot topologies
with the number of rotor poles limited to 5, 7, 8, 10, 14 and the 24 stator-slot
topologies with number of rotor poles limited to 10, 14, 16, 20, 22 were investigated.
5
A coil test analysis was performed for feasible topologies of SalRoN WFFSM to
confirm the operating principle. Assuming that only a water cooling system was
employed, the limit of the current density was set to the maximum 30 Arms/mm2 for
armature winding and 30 A/mm2 for FEC, respectively. The electromagnetic
performance, including back EMF, cogging torque, and average torque had been
analysed and compared using 2D-FEA. The torque-speed characteristics were
evaluated by varying the armature phase angle, θ. The iron and copper losses were
calculated based on 2D-FEA and formula, which assisted in calculating the efficiency
of the proposed SalRoN WFFSM. The design restrictions, target specifications, and
parameters of the proposed SalRoN WFFSM were based on the WFFSM employing
a segmented rotor and non-overlapping windings. The outer diameter, the motor
stack length, the shaft radius, and the air gap, having dimensions 150 mm, 70 mm, 24
mm and 0.3 mm, respectively, were kept constant. The electrical restrictions related
with the inverter such as maximum 415V DC bus voltage was set similar as in the
WFFSM with a segmented rotor and non-overlapping windings. The field current
applied to SalRoN WFFSM was limited to 50 A.
1.5 Motivations for Research
For the past 10 years, the automotive, aerospace and shipbuilding industries have
been working to design electric motors to improve the efficiency, torque and power
as well as minimise the cost. In order to reduce the cost, rare earth material has been
removed from the existing PM electric machines and their various characteristics are
examined. Moreover, the efficiency is improved by employing non-overlapping
windings that reduce the copper loss. The performance of WFFSM has been
investigated, in response to economical and environmental pressures. As the
capabilities of semiconductor devices and power converter grow, improvements in
the performance of the WFFSM and considerations of new configurations are
required.
The desktop workstation of modern technology has high processing power
and speed and handles repetitive design problems with an ease not experienced
before. JMAG tool with numeral analysis function for electric machine design using
2D and 3D-FEA are now routinely applied in design, analysis and optimisation of
6
machine dimensions. In the design and analysis of SalRoN WFFSM of this study,
extensive use of 2D and 3D-FEA has been applied.
1.6 Contribution to Knowledge
The contributions of this research are as follows:
(i) Various structures of WFFSM have been reviewed and published.
(ii) It was explained that SalRoN WFFSM is particularly suitable for low cost
and high-speed applications. A novel structure of light weight, more
efficient, and robust rotor WFFSM was validated by 2D-FEA. This thesis
elaborates the feasible topologies for three-phase SalRoN WFFSM.
(iii) Deterministic optimisation and GA methods were adopted to enhance the
motor characteristics and compared with the existing designs of
WFFSMs. The optimized design has achieved better characteristics than
the existing designs and published.
(iv) Different methods were applied to reduce the cogging torque effect and
the flux linkage were made sinusoidal by the rotor pole width variation.
(v) 3D-FEA modelling was examined for the precise analysis of SalRoN
WFFSMs.
1.7 Thesis Organisation
This thesis deals with the design and optimisation of SalRoN WFFSM for high-speed
applications. The thesis is divided into six chapters and the summary of each chapter
is listed as follows:
(i) Chapter 1: Introduction
The first chapter explains the importance of magnetless high-speed
electric machines and provides the broad context in which the motivation
and research background with this work are embedded. The problems of
current WFFSMs are highlighted and research objectives to solve the
problems together with the major contributions are outlined in this
chapter.
7
(ii) Chapter 2: Overview of Flux Switching Motors (FSMs)
The second chapter is a literature review that summarises the basic theory
of flux switching and classification of FSM including the examples of
PMFSM, FEFSM, and HEFSM. The structures, modelling techniques,
and various characteristics of these FSMs are discussed in detail and
compared. In the last section, a brief explanation is provided for structure
review, flux linkage, cogging torque, average torque, efficiency, and
analytical modelling of FEFSM.
(iii) Chapter 3: Design Methodology
The third chapter describes the design methodology of the proposed
SalRoN WFFSM using commercial 2D-FEA, JMAG-Designer ver. 14.1,
released by JSOL Corporation. Design process, coil arrangement test, and
performance analysis are highlighted to investigate the performance of
various topologies of SalRoN WFFSM. In a later section, the procedure
of deterministic optimisation and GA methods are explained to treat
various parameters of the machine and enhance its characteristics.
(iv) Chapter 4: Characteristics Investigation of the Proposed SalRoN WFFSM
In this chapter, the principle of flux switching by means of a salient rotor
is portrayed with the help of elementary structure, and a calculating
method of average torque is introduced for SalRoN WFFSM. Further
design evaluations based on 2D-FEA and the changing pattern of 12S-8P
SalRoN WFFSM characteristics with the variation of rotor pole width are
presented in this chapter. Torque density, power density, and efficiency
are calculated for the initial designs of SalRoN WFFSMs.
(v) Chapter 5: Design Optimisation
Among the various slot combinations of SalRoN WFFSM discussed in
chapter 4, the 12S-8P, 12S-10P, 12S-14P, and 24S-14P are optimised
using deterministic optimisation and GA methods until the target
performances are achieved. The results of the initial and optimised design
that met the target performances are analysed and discussed. Various
cogging torque reduction techniques are adopted to minimise the effect of
cogging torque. Moreover, this chapter also explains 3D-FEA modelling
of the design for precise analysis of axial flux.
8
(vi) Chapter 6: Conclusion and Future Works
The final chapter describes the major results and concludes the summary
of the research as well as recommendations for future work.
CHAPTER 2
OVERVIEW OF FLUX SWITCHING MOTORS (FSMs)
This chapter reviews the types of rotating electric machine based on the principle of
flux switching. It explains the flux switching mechanisms of different FSMs types,
from the early concepts to the modern designs. The merits and demerits of various
FSMs as well as numerous approaches to evaluate their performances are also
highlighting. As the thesis is on WFFSMs that employ salient rotors, the last section
provides more detail and significance of these machines.
2.1 Introduction
The variation of permeance seen by armature with respect to the rotor position
changes the armature flux between the maximum (high state) and minimum (low
state) values, and introduces a new term called ‘flux switching’. Electric machines
that operate on this principle are called flux switching machines. The theoretical
design of the inductor alternator based on flux switching has been known since 1940s
[7], but the analytical approach appears to have come into use a decade later [25]. In
[26], a PMFSM, i.e. PM single-phase limited angle actuator, or more well-known as
Laws’ relay, has four stator slots and four rotor poles developed, while in [25] it was
extended to a single-phase generator with four stator slots, and four or six rotor
poles. Research work has been conducted on these machines for several years
without using the term flux switching [27-30]. During the development of power
electronics technology in the late 1990s, this term was used and investigated [31],
[32]. Computer-aided design (CAD) tools with numeral analysis functions, normally
Finite Element Analysis (FEA) using 2D or 3D, contributed a lot in design, analysis,
10
and optimisation of FSM. Over the past ten years or so, many novel FSM topologies
have been developed for various applications, ranging from low-cost domestic
appliances, automotive, wind power, and aerospace.
2.2 Operation and classification of the Flux Switching Machine
In the mid-1950s, the term ‘flux switching’ was used to explain an inductor
alternator with bipolar armature flux linkages [25]. Figure 2.1(a) and (b) illustrate the
simple mechanism of flux switching alternator. A pair of stator windings, a dual set
of laminated yolks, and a pair of PMs were located on the stator, while the rotor was
shown as a two salient pole stacks of laminations on the shaft. The flux paths shown
by arrows in Figure 2.1(a) indicate the flow of the flux from left to right in both
windings. When the rotor position was moved by a half-electrical cycle, as in Figure
2.1(b), the flux linkage had the same magnitude but the direction had been reversed
as in Figure 2.1(a). A complete reversal of flux was attained by each revolution of
the rotor. Consequently, the salient pole of the stationary part and stator operated in a
conventional pulsating flux manner.
The PM of inductor alternator was replaced by appropriate field windings
without altering the basic performance [32]. The required resultant flux orientation
was supplied by a field winding with unipolar current and armature windings with
single-phase current. The operation principle of flux switching motor without
(a) (b)
Figure 2.1: A flux switching inductor alternator [25]
11
magnets could be described with the aid of Figure 2.2. Two possible aligned
positions of the rotor were shown by cross-sectional views of the motor.
Conventional cross and dot notations were used to indicate the path of current flow
in the armature and field windings.
The combined resultant flux created by field and armature windings travelled
in the northerly vertical direction; aligned the rotor with vertical stator poles, as
illustrated in Figure 2.2(a). Considering Figure 2.2(b), the current in the armature
winding was reversed for the next half cycle, while the field winding remained
excited in the same direction causing the resultant flux to flow in the westerly
direction, which tended to align the rotor with horizontal stator poles. Overlap
armature and field windings has been caused copper losses in this motor and thus
reduced the efficiency.
There are three classes of FSMs, namely permanent magnet FSM (PMFSM),
field excitation FSM (FEFSM), and hybrid excitation FSM (HEFSM). They are
broadly defined and differentiated by field flux source i.e PM or field winding and
both PM and field winding, as illustrated in Figure 2.3.
(a) (b)
Figure 2.2: Basic operation principle with constant field winding excitation and single-phase armature current, (a) Armature flux linkage-positive and
(b) Armature flux linkage-negative [32]
×
×
××
F
F
F
F
A
A
A
A
××
××
F
F
F
F
A
A
A
A
2.3 Permanent Magnet Flux Switching Motor (PMFSM)
Over the
various
expensive to fabricate. Furthermore, the torque ripple must be considered
caused by severe magnetic saturation and irregular variation of winding inductances
[33]. The PMFSM with PM embedded in the rotor has less robust structure and
cannot be used for high
practically applied in industrial and domestic applications.
2.3.1 Various Configurations of PMFSMs
Various configurations of PMFSMs have been proposed by researchers worldwide to
attain better characteristics in term
development and various structures have been overviewed in [34]. For low energy
axial fan applications, inexpensive ferrite magnet 4S
cheap solution in [35]. Numerous PMFSM topologies [36
recently, they are mentioned as follows:
(i)
(ii)
(iii)
(iv)
Permanent Magnet Flux Switching Motor (PMFSM)
Over the past decade, PMFSM has been attracting a lot of research interest for
applications. The PMFSM has high
expensive to fabricate. Furthermore, the torque ripple must be considered
caused by severe magnetic saturation and irregular variation of winding inductances
[33]. The PMFSM with PM embedded in the rotor has less robust structure and
cannot be used for high-speed applications [24].
Due to the aforementioned demerits,
practically applied in industrial and domestic applications.
.1 Various Configurations of PMFSMs
Various configurations of PMFSMs have been proposed by researchers worldwide to
attain better characteristics in terms
development and various structures have been overviewed in [34]. For low energy
axial fan applications, inexpensive ferrite magnet 4S
cheap solution in [35]. Numerous PMFSM topologies [36
recently, they are mentioned as follows:
(i) Single-phase, three-phase, and multiphase PMFSMs [43], [34]
(ii) Fault tolerant PMFSMs [38]
(iii) Tabular PMFSM and Transverse flux PMFSM, [39],
(iv) Outer and Inner rotor PMFSMs [41]
Figure 2.3: Classifications of
Flux Switching Motors (FSMs)
Permanent magnet(PM) FSM
Field Excitation (FE) FSM
Permanent Magnet Flux Switching Motor (PMFSM)
ast decade, PMFSM has been attracting a lot of research interest for
applications. The PMFSM has high magnet-consuming complex stator and
expensive to fabricate. Furthermore, the torque ripple must be considered
caused by severe magnetic saturation and irregular variation of winding inductances
[33]. The PMFSM with PM embedded in the rotor has less robust structure and
speed applications [24].
Due to the aforementioned demerits, the PMFSMs have not
practically applied in industrial and domestic applications.
.1 Various Configurations of PMFSMs
Various configurations of PMFSMs have been proposed by researchers worldwide to
of torque, speed, power, and efficiency. The
development and various structures have been overviewed in [34]. For low energy
axial fan applications, inexpensive ferrite magnet 4S-4P PMFSM was proposed as
cheap solution in [35]. Numerous PMFSM topologies [36-42] have been developed
recently, they are mentioned as follows:
and multiphase PMFSMs [43], [34]
Fault tolerant PMFSMs [38]
Tabular PMFSM and Transverse flux PMFSM, [39], [40]
Outer and Inner rotor PMFSMs [41]
Figure 2.3: Classifications of FSM
Flux Switching Motors (FSMs)
Field Excitation (FE) FSM
Hybrid Excitation(HE) FSM
12
ast decade, PMFSM has been attracting a lot of research interest for
consuming complex stator and is
expensive to fabricate. Furthermore, the torque ripple must be considered, which is
caused by severe magnetic saturation and irregular variation of winding inductances
[33]. The PMFSM with PM embedded in the rotor has less robust structure and
the PMFSMs have not yet been
Various configurations of PMFSMs have been proposed by researchers worldwide to
and efficiency. The
development and various structures have been overviewed in [34]. For low energy
4P PMFSM was proposed as a
42] have been developed
and multiphase PMFSMs [43], [34]
Hybrid Excitation(HE) FSM
13
(v) PMFSMs with single-tooth or multi-tooth per pole [42]
(vi) E-core and C-core PMFSMs [44], [45]
(vii) Segmental rotor PMFSM [46]
Figure 2.4(a) illustrates a typical three-phase 12S-10P PMFSM, where the
stator consists of concentrated armature winding, and each tooth is being wounded
by a coil. A PM was placed between U-shaped laminated segments and the polarity
of PM was reversed from one magnet to another [43]. For three-phase PMFSM,
alternate poles wound windings were investigated to be fault tolerant, as shown in
Figure 2.4(b) [38]. However, these PMFSMs had the disadvantage of high magnet
volume. To reduce the volume of PM, a new structure of E-core PMFSM was
developed by replacing the alternate wound pole with a simple stator tooth, as
illustrated in Figure 2.4(c) [44]. Furthermore, to enhance the characteristics of E-core
PMFSM, the stator tooth was removed to enlarge the slot area and as a result C-core
PMFSM was developed, as illustrated in Figure 2.4(d). Additionally, the multi-tooth
structure of PMFSM, discussed in [42], was utilised to improve the torque density
and reduce magnet usage, as in Figure 2.4(e). A three-phase segmental rotor PMFSM
was also reported, as shown in Figure 2.4(f). These kinds of machines have less
robust structure, which need to be considered if they are applied for high-speed
applications.
2.3.2 Modelling Techniques of PMFSMs
Numerous modelling techniques have been developed for PMFSMs and can be
generally divided into two categories: analytical and numerical. The analytical
approaches that are usually developed for specific geometry and topology are not as
versatile as the numerical ones and might lead to inaccuracy. In contrast, the
numerical measures, which are analysed with 2-D or 3-D FEA, present more precise
evaluations for even complex geometry. However, 3-D FEA that involves several
repetitive computations is extremely time-consuming for optimisation. Sizing-
designing procedure of the PMFSM based on simplified analytical model is
presented in [47]. Furthermore, the magnetic equivalent circuit (MEC) methods have
been widely applied to model the PMFSM more accurately compared with analytical
method. 12S-10P PMFSM was optimised and analysed by a new non-linear adaptive
14
(a) (b)
(c) (d)
(e) (f)
Figure 2.4: Topologies of PMFSMs. (a) 12S-10P PMFSM with all poles wound, (b) PMFSM with alternate poles wound, (c) E-core PMFSM, (d) C-core PMFSM,
(e) Multi-tooth PMFSM, (f) Segmental rotor PMFSM with all poles wound
A1 A1
C1
A2
A2
A1
B1
B1
B1
C1 C1
B1
C1
B2
C2
B2
C2
A1
C1
A1
B1
B1 C1
C1
A1
B1
B1 C1
A2
C2
A2 B2
B2
C2
C1
A1
B1
B1
C1
A1 A1
C1 B1
B1 C1
15
lumped parameter MEC model [48]. Additionally, the PMFSM model was patched to
analyse with iron bypass bridges [49]. For the radial flux PMFSM, 2-D FEA had
been routinely employed as it could predict the performance with short
computational time [50]. However, the 2-D FEA results are less precise due to
assumption of zero axial flux.
2.4 Hybrid Excitation Flux Switching Motor (HEFSM)
A non-exhaustive review of HEFSM literature was presented in this section.
HEFSMs are those that utilise two excitation flux sources: PM as well as FEC
source, as shown in Figure 2.5 [51], [52]. HEFSMs have been investigated widely
over many years and have the potential to provide high torque and power density,
high efficiency, and variable flux capability [11], [53-55].
A 6S-4P HEFSM is shown in Figure 2.5(a), which consisted of armature
winding, field winding, and PM, arranged in three layers in the stator [56]. However,
this configuration had long end DC windings, which increased copper loss and
reduces efficiency. A novel 12S-10P HEFSM was discussed in [53], in which the PM
was placed between the stator segments leaving enough space for DC FEC, as
depicted in Figure 2.5(b). The flux regulation capability of HEFSM can be controlled
by adjusting the dimensions of PM in radial direction.
Non-overlapping armature and field windings were employed in the new
structure of E-core HEFSM, as shown in Figure 2.5(c) [55]. The slot area for both
FEC and armature winding were equal with same number of turns. Recently, three-
phase E-core HEFSM with non-overlap windings and reduced PM size, as depicted
in Figure 2.5(d), was analysed in [57]. The performance of E-Core HEFSM in terms
of flux capability, torque, and power versus speed curve was also been examined.
The proposed machine prides itself on the merits of lower cost and less copper.
The aforementioned HEFSMs with active components on the stator suffered
from these disadvantages:
(i) Both the PM and FEC were in series with each other in Figure 2.5(a), which
limited the flux-adjusting capacity owing to low permeability of PM.
(ii) The main flux generated by PM for maximum torque production was reduced
by the flux path of DC FEC, Figure 2.5(b).
16
(iii) In Figures 2.5(b), (c), and (d), the PM was placed at the outer surface on the
stator. Hence, the flux of PM acted as a leakage flux and had no involvement
in torque generation.
(iv) The HEFSM was also difficult to manufacture due to segmented stator core,
Figure 2.5(b) and (c).
(v) Torque density might be reduced because of less PM volume, Figure 2.5(d).
(a) (b)
(c) (d)
Figure 2.5: HEFSM examples, (a) 6S-4P HEFSM, (b) Three-phase 12S-10P HEFSM, (c) 12S-10P E-core HEFSM and (d)6S-8Pole E-core HEFSM
FEC
FEC
PM PM
A1
A1
B1
B1
C1
C1 FEC-1
FEC-2
A1 A1
A2
A2
B1
C1
B1
C1
B2
C2
B2
C2
A1 A1
B1 C1
B1 C1
FEC-1
FEC-2
FEC-1
FEC-2
FEC-1
FEC-2
B1
C1 B1
A1
C1 FEC-2
FEC-1
FEC-2
FEC-1
17
2.5 Field Excitation Flux Switching Motor (FEFSM)
The quest for low-cost, high efficiency and simple configuration electric machines is
ongoing process. As the annual consumption and the cost of rare-earth material have
increased over the past decade, the prices of Neodymium (Nd) and Dysprosium (Dy)
used in PMFSM and HEFSM rise markedly which creates problems of supply
shortages and security issues. To overcome this issue, the excitation on the stator of
conventional PMFSM can be easily replaced by DC FEC to form field excitation flux
switching motor (FEFSM). In other words, the FEFSM is a form of salient-rotor
reluctance machine with a new topology. The concept of the FEFSM involves
changing the polarity of the flux linking with the armature winding, with respect to
the rotor position. The FEFSM has advantages of low cost, simple construction,
magnet-less machine, and variable flux control capabilities suitable for various
performances when compared with others FSMs. Many topologies of FEFSM have
been studied and documented [1], [5], [15], [20], [21], [32], [58-61].
2.5.1 Structure review of FEFSM
Early examples of single-phase 4S-2P FEFSM that employ a DC FEC on the stator, a
toothed-rotor structure, and fully-pitched windings on the stator were discussed [59].
Both the armature and field windings were placed in the stator, which overlapped
each other and produced high copper losses. This design is practically used in
various applications that require high power densities [60]. Single-phase AC and DC
were applied to armature and field winding of this machine, respectively. The
maximum flux interaction required for the rotation of rotor was supplied by armature
coil at zero rotor position and the torque was produced by the variable mutual
inductance of windings. The single-phase FEFSM can be considered as a simple
machine that required two powered electronic controllers for armature and DC FEC.
The main advantages of this design are low cost for high volume applications and
precise control of position, torque, and speed.
Another example of FEFSM is depicted in Figure 2.6(a) with eight stator
slots (four slots for armature coil and four for FEC) and four rotor poles. The design
specifications and operation of 8S-4P FEFSM were explained in [61]. When
18
compared with induction machine, the FEFSM had achieved high torque and
efficiency but the main problems concerned with this design are low starting torque,
high torque ripples, overlapped windings, and fixed rotating direction. Two single-
phase FEFSMs topologies with DC field and AC armature windings with the same
coil-pitch of two slot-pitches and different coil-pitches of one and three slot-pitches
respectively were discussed [6]. It is shown that the iron loss of FEFSM had been
reduced and thus increased the efficiency. These machines shared the same operating
principle as discussed in [61], but 12S-6P explained in [6] had much shorter end
windings, and therefore, much better copper usage efficiency. These topologies had
problems of overlap windings and high copper losses. The structure of single-phase
(a) (b)
(c) (d)
Figure 2.6: Single-phase FEFSMs, (a) Single-phase 8S-4P FEFSM, (b) single-phase 12S-6P FEFSM with salient rotor, (c) single-phase 8S-8P FEFSM with overlapping windings, (d) single-phase 12S-6P FEFSM with segmental rotor
A1
A1
A1
FEC
FEC-2
A1
A1 A1
FEC FEC
FEC
FEC-1
A1
A1
19
FEFSM is illustrated in Figure 2.6(b). The performance analysis of single-phase 8S-
8P FEFSM, depicted in Figure 2.6(c), was discussed in [62]. The proposed motor has
high cogging torque and overlap armature and field windings which made it
unsuitable to be applied for any electrical equipment. A single-phase 12S-6P FEFSM
for high density air conditioner with segmental rotor was designed and discussed in
[63]. The proposed motor had less copper losses due to non-overlap armature and
field windings as shown in Figure 2.6(d). Although 12S-6P had high average power,
the rotor was not robust due to segments, hence could not be used for high-speed
applications.
The PM of 24S-10P PMFSM was replaced by FEC to design a three-phase
FEFSM, as illustrated in Figure 2.7(a). The total flux generation was limited due to
the isolation of DC FEC and thus reducing the performances [14]. To improve the
drawbacks of FEFSM, 12S-8P FEFSM with segmental rotor was designed and
experimentally tested [20]. Concentrated winding arrangement was used in this
design, which gave shorter end windings of DC FEC and armature coil when
compared with the tooth rotor structure with distributed windings. This design had
significant gains over other designs as it utilised less conductor materials, thus
improving the overall efficiency due to the reduction of copper loss. FEFSMs with
single and dual polarity FEC were discussed in [21], [5], [64]. The advantages of
FEFSM with single polarity FEC are low copper loss due to less volume of FEC, less
leakage flux when compared with dual FEC windings. The field-weakening
capability of FEFSM was improved using toroidal DC field winding [22]. The
proposed machine had limited torque generation due to the field flux produced by
DC field conductors close to the outer surface of the stator, which went through the
outside of the stator instead of the rotor as well as high copper losses owing to
overlap armature and field windings.
In recent years, research on in-wheel motor for EV drive train system has
become more popular due to their several advantages of independent wheel
controllability and higher efficiency. In addition, it provides more cabin space caused
by the elimination of mechanical transmission gears as conventionally used in most
existing EVs with single motor propulsion system configuration. Since the outer-
rotor configuration was more suitable for direct drive, the PMFSM with outer-rotor
had been proposed only for light EV applications [65]. It provided essentially
sinusoidal back-EMF and high torque at low speed. Nonetheless, constant PM flux of
20
PMFSM made it difficult to control, which required field weakening flux at high
speed conditions. 12S-10P outer rotor FEFSM had been proposed and discussed in
[66], as illustrated in Figure 2.7(b). Robust rotor structure with high mechanical
strength and no PM were clear advantages of this machine while overlap windings
will create problem of high copper losses. Three types of low-cost FEFSMs with DC
field and AC armature windings with the same coil pitch of one slot pitch (12S-8P),
two slot pitches (12S-5P and 12S-7P machines), and different coil pitches of one and
three slot pitches (9S-5P), respectively, were analysed and compared in [67]. It was
concluded that halving stator slots and rotor poles number can be an effective
approach to increase density for FEFSMs.
2.5.2 Design restrictions and specifications for FEFSMs
The design specifications of FEFSMs are illustrated in Table 2.1 in which three
major parameters; stator radius, rotor radius and torque density were chosen to
differentiate FEFSMs from one another and be further explained in terms of their
characteristics. The operating principle of flux switching was obeyed by all these
designs. According to the rotor rotation, the flux flows generated by PMs and mmf of
FECs were switched and linked with the armature coil alternately while for FEFSM
there was no PM, the armature winding and the field excitation coil both were
stationary but the magnetic flux linkage in the armature winding could either be
(a) (b)
Figure 2.7: Three-phase FEFSM, (a) Three-phase 24S-10P FEFSM, (b) three-phase outer rotor FEFSM
A1
A2 C1 B1 B2
C2
A1
A2 C1 B1 B2
C2
FEC-2 FEC-1
FEC-1 FEC-2
FEC-1 FEC-2
FEC-1
FEC-2 A1
B1
C1 A2
B2
C2
A3
B3
C3 A4
B4
C4
21
positive or negative depending on the position of the mobile part. The flux generated
by field excitation coil flowed from stator to rotor and then from rotor to stator to
produce a complete cycle.
2.5.3 Flux linkages of various FEFSMs
A key factor for all developed FEFSM models was the phase flux linkage
calculation, which created a significant challenge, since the stator had salient poles
and the iron core saturation had a significant influence on the motor’s operation.
Many research works were published in the past decade in this domain, as [68] that
introduced analytical models to calculate the flux linkage, [69] that developed
models based on magnetic equivalent circuits, or [70] where the analytical model
was created using FEM analysis results. Deterministic optimisation and GA were
usually applied for the improvement of flux linkage. Additionally, swarm
optimisation [71] could be used to treat several parameters of motor to improve the
flux linkage. Although the flux linkage strength of segmental rotor FEFSM was high
due to short flux path as compared to salient rotor, the rotor was not robust due to
segments, as illustrated in Figure 2.8. All the FEFSMs with salient rotor were the
best candidates to be applied for high-speed applications.
Table 2.1: FEFSMs Comparison
Types of machines Stator radius (mm)
Rotor radius (mm)
Torque density
8S-4P FEFSM 45 25 Not mentioned
Single-phase FEFSM with salient rotor
45 25 Not mentioned
Single-phase FEFSM with segmental rotor
75 44.5 Low torque density due to saturation of rotor segments
Three-phase 24S-10P FEFSM
45 29.25 Less torque density compared to PMFSM
Three-phase 12S-8P FEFSM (segmental rotor)
75 45 Low torque density due to saturation of rotor segments
Three-phase 24S-10P (dual FEC)
132 97.2 8.09Nm/kg
Three-phase 24S-10P (single FEC)
132 97.2 Potentially good due to less FEC windings
Three-phase 12S-14P FEFSM (toroidal DC
winding)
240.3 158 Improvement in field weakening, High torque density compared with
PMFSM Three-phase outer rotor
FEFSM 109.5 132 2.63Nm/kg
22
2.5.4 Cogging torque of FEFSMs
Cogging torque did not add to electro-magnetic output torque. It only effects in
torque pulsations that corresponded to undesirable vibration and acoustic noise. The
number of periods, Np of the cogging torque waveform over a rotation of one stator
tooth pitch was given by [20];
],[ rotorst
rotorp NNHCF
NN (2.1)
where the denominator is defined as the highest common factor (HCF) between
stator slots, Nst and number of poles of the rotor, Nrotor. Using the index Np, the
electrical angle of rotation, αcog for each period of the cogging torque and the number
of periods of cogging torque, Nelec per electrical cycle are therefore,
stpcog NN
0360
(2.2)
rotor
stpelec N
NNN (2.3)
(a) (b)
Figure 2.8: Flux distribution, (a) Flux lines of segmental rotor and (b) salient rotor
Long flux path Short flux path
B[T] 2.8T
2.1T
1.4T
0.7T
0T
23
Various techniques had been published to reduce the cogging torque on both
radial type [72-74] and axial type PMFSM [75], left vacant space in the area of
FEFSMs, as all the designs discussed above had cogging torque especially various
topologies of three-phase FEFSM, which had high cogging torque, as shown in
Figure 2.9 [64]. Rotors with stepped skew [76, 77] could be adopted to reduce the
cogging torque and torque ripple under various load conditions. Different kinds of
notching schemes [78, 79] were also available for cogging torque reduction.
2.5.5 Average torque and efficiency
The electromagnetic torque, Te developed in an electrical machine generally
consisted of a reluctance torque component, Trel and an excitation torque component,
Texc, and might be expressed in a polyphase arrangement as [20],
k
kexck
krele TTT ,,
(2.4)
dd
iddL
iT exck
kk
k ke 221
(2.5)
Figure 2.9: Cogging torque of three-phase FEFSM [64]
-40
-30
-20
-10
0
10
20
30
40
0 60 120 180 240 300 360
T [Nm]
Electric cycle [°]
12S-10P 12S-14P 12S-16P12S-20P 12S-22P
24
where Lk is the phase winding inductance, ψexc is the flux linkage due to field
excitation, ik is the phase current, θ is the electrical angular position of the rotor, and
k= a, b, c is the phase designation. As the operation of the FSM with sinusoidal
current was with the current placed in phase with the back-EMF, the principal torque
was due to Texc and the contribution of Trel was negligible, so that Te can be expressed
as
k
kexcr
kkk
r
ie T
titetP
T ,
)()()(
(2.6)
with Pi being the instantaneous power, ωr the rotational speed, and ek the
phase back EMF. The flexible characteristic of the average torque, controllable by
both the field and armature current was one of the major advantages of FEFSMs
when compared with PMFSM. The first FEFSM developed a torque of just under 1.2
Nm at a speed of 9,500 r/min corresponded to a peak power output of 1170 W,
examined in [59]. Peak efficiency of the complete drive was measured at just less
than 50%, which was lower than anticipated. The maximum efficiency obtained for
8S-4P FEFSM drive was about 75% at various torque level but the average torque
needed improvement at approximately 2 Nm. In [14], the electromagnetic
performance of the 12S-10P, 12S-11P, 12S-13P, and 12S-14P FEFSMs were
investigated by 2D-FEA analysis and validated experimentally. The average torque-
current characteristics of various rotor pole configurations are illustrated in
Figure 2.10. The experimental results illustrated that slightly larger torque was
produced by 24S-10P FEFSM when compared with 24S-10P PMFSM at lower field
current. As the field current increased, at certain levels the stator teeth were saturated
and the FEFSM exhibited much lower torque.
A few investigations were undertaken for segmental rotor FEFSM but
researchers agreed that this topology was particularly attractive for low-cost
operation due to non-overlapping windings and no permanent magnet [20]. The
mean torque output increased proportionally with the armature current and field
current. At rated field and armature current, the output mechanical torque was
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