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Improved Design ,and Performance Analysis of a Claw Pole Permanent MagnetSMC Motor with Sensorless Brushless DC D riveY. G. Guo' , J. G. Zhu', P. A . Watterson', W. M. Holliday', and W. Wu2'Faculty of Engineering, University of Technology, Sydney, P.O. Box 123, Broadway, NSW 2007, Australia

'CSIRO Telecommunications and Industrial Physics, P.O. Box 218,Lindfield, NSW 2070, Australia

Abstract-This paper presents a three-phase claw polepermanent magnet soft magnetic composite motor, whichwas designed to take advantage of specific properties of thematerial. Parameter calculations by the finite elementmagnetic field analysis and performance prediction by theequivalent circuit are discussed. To verify the theory, aprototype motor was constructed and operated by asensorless brushless dc drive scheme. The experiment resultsare reported and show good c orrelation with the theory.

Keywords-Claw pole motor, finite element analysis,sensorless brushless dc drive, soft magnetic composite.

I. INTRODUCTIONSoft magnetic composite (SMC) materials possess anumber of advantages over traditional laminated steelscommonly used in electromagnetic devices and haveundergone a significant development in the past few years[l]. SMC material is made of iron powder of high purityand compressibility. The grains are coated with an organicmaterial, which provides the bonding and produces a highelectrical resistivity. The coated powder is then pressed ina die to form a solid part and finally heat treated to annealand cure the bond. There is usually no further machiningrequired, and product cost is much lower than punching,

stacking and welding of laminations.The unique properties of SMC materials includethree-dimensional (3D) isotropic ferromagnetic behavior,very low eddy current loss, relatively low total iron loss atmedium and high frequencies, and higher thermalconductivity than across laminations (though lower thanwithin laminations). To investigate the potential of SMCmaterials, a lot of work has been conducted andencouraging improvement has been achieved in both thematerial and its application in electrical machines [2,3].In this paper, a small three-phase three-stack clawpole permanent magnet (PM) motor with SM C stator hasbeen designed and constructed to take advantage of theproperties of SMC materials. 3D finite element magneticfield analysis was conducted for major parametercalculation and dimension optimization. The design andperformance analyses are validated by experimental testson the prototype, which is driven by a sensorlessbrushless dc drive scheme. Both the method and results ofthe experiment are reported in detail below.The stator core material is SOMALOY" 500 [4], anew soft magnetic composite produced by Hoganas AB,

Sweden. It is characteriz.ed by a thin continuous surfaceinsulation layer with little or no effect on the powdercompressibility. This malerial was specially developed forsoft magnetic applications with 3D magnetic fluxes, suchas electrical machines.Although the motor prototype in this paper wasmanufactured by cold machining from available performs,the compression molding technique would be used forcommercial mass production.

11. SMC PROPERTIES EXPLOITEDN MOTORDESIGNThe powdered nature of the SMC material yieldsisotropic magnetic propexties, which opens up the crucialdesign benefit of employing 3D flux paths. The 3Dmachine explored here is a claw pole structure, which isvery difficult to manufacture by using laminated steels.Taking advantage of the isotropic magnetic property ofSMC material, the magnet axial length in the prototypecan be designed longer than the claw pole to obtain higherstator flux and then higher specific torque. Besides theradial direction, the flux can also flow into the SMC clawpoles via the side surfaces. By contrast, laminated steelsare effective in carrying varying magnetic flux only in theplane of laminations while maintaining low eddy currentloss.The isotropic thermal property of SMC materials isalso advantageous in increasing heat dissipation from theinternal stator of the motor described here. For laminatedsteels, the thermal conductivity in the directionperpendicular to the lamination plane is much lower thanthat within the plane. This implies that in laminated coresthe heat is transferredl almost uniquely at laminationedges. For the claw pole stator here, SMC use impliesadditional cooling from the teeth sides which wouldimprove the heat dissipation.Because the iron particles are insulated by the surfacecoating and adhesive, which is used for compositebonding, the eddy current loss is much lower than that inlaminated steels, especially at higher frequencies. Thetotal loss is dominated by hysteresis loss, which is higher

than that of laminaled steels due to the particledeformation during compaction. At the power frequency50 Hz and 1.5 T, the total core loss in SomaloyTM 00(with 0.5% Kenolube) is 14 W/kg [4], double that of eventhe low grade Kawasaki 65RM800 (0.65 mm thick, 28 x10' Qm) [5]. When the excitation frequency increases,however, the increment of core loss in SMC is smaller

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than that in electrical steels due to the smaller eddycurrents. At 400 Hz and 1.5 T the total core loss inSomaloyTM 00 is the same as the low-medium gradeKawasaki 50RM700 (0.5 mm thick, 28 x lo-' Qm),namely 120 W/kg. High grade Kawasaki 35RM270 (0.35mm thick, 54 x IO-* Qm ) has one third the loss then, i.e.40 Wikg at 400 Hz and 1.5 T. Thus, SMC materials aremore likely to be better used for motors operating athigher excitation frequencies, but they are not yet as goodas high grade laminations at low and medium frequenciesand any superior performance must come from exploring3D flux topologies or some other SM C feature.The permeability of SMC material is lower than thatof electrical steels because it has less ful l density. Bestfigures are in the range of 50 0 for maximum relativepermeability [4]. It is expected that this material would beappropriate for construction of PM motors for which themagnet reluctance dominates the magnetic circuit, makingsuch motors less sensitive to the permeability of the corethan armature magnetized machines, e.g. induction andreluctance machines. In spite of the lower value, thepermeability of SM C is much more stable with respect tothe frequency than that of electrical steels. SM C canmaintain nearly a constant magnetic permeability up to aquite high frequency. This is a favorable property formotors operating at higher frequencies.The saturation flux density is reduced as compared tothe base iron powder. Hog anb AB reports that SomaloyTM500 has a flux density of 2.37 T at 340 kA/m [4], which is1.94 T above that for air at that field strength, comparedto 2.18 T for perfectly aligned iron. To help compensatefor the reduced saturation flux density and increased coreloss, the prototype is designed to have lower magneticflux density in iron components, e.g. only about 1.0 T inthe stator yoke.

111. PROTOTYPEOTORFig. 1 illustrates the magnetically relevant parts of therotor an d the stator of the prototype. Table 1 lists thedimensions and major parameters. The three phases of themotor are stacked axially. Each stator phase has a singlecoil around an SM C core, which is molded in two halves.The outer rotor comprises a tube of mild steel with anarray of magnets for each phase mounted on the innersurface. Mild steel is used for the rotor because the fluxdensity in the yoke is almost constant.For the prototype, the motor size and core geometrywere to a large extent determined by the dimensions ofthe available SomaloyTM00 preforms. They were chosen

the same as those .of a PM SM C transverse flux motorprototype [6], in order to simplify comparison betweenthe two topologies. A pole number of 20 was chosengiving an operating frequency of 300Hz at 1800 rpm. It isnot an unrealistically high frequency to work at for SM Cmaterials. Since a simple concentrated stator winding isused, the fill factor is higher and the manufacturing cost

lower compared to a conventional multi-coil windingwound between teeth.

(a) Rotor

(b) Three-stack stator coresFig. 1. Magnetically relevant parts of the claw pole motor

TABLEDIMENSIONS AND MAJORPARAMETERS

Dimensions and parametersRated frequency (Hz)Number of phasesRated power (W )Rated line-to-neutral voltage (V)Rated phase current (A)Rate d sp eed (rev/")Rated torque (Nm )Rated efficiency (%)Rated temperature rise ("C)Numbe r of polesStator core inaterial

Quantities30 0350 0644. 018002.65807520SOMALOYTM 00Stator outer radius (mm)Effective stator axial length ( m m )Total motor length ( m m )Rotor (and motor) outer radius (mm)Rotor inner radius (mm)Permanent magnetsNumber of magnetsMagnet dimensionsMagnetization directionsMain airgap length (mm)Sub-airgap length* ( m m )Stator shaft materialShaft outer radius (inm)Numbe r of coilsCoil window dimension (mm')Number of turnsNumber of strandsDiameter ofcopper wire (mm)

Resistance at 1 15C (Q)Self inductance for each phase (mH)Armature reaction in magnets (T)

409313 74741NdFeB, Grade N30M60OD88 x ID82 x 15 m m arc 12"Radially outward and inwardI4. 2Mild steel931 7 x I I750. 70.3025.240.033

?

Cogging torque of 6"' harmonic (Nm)* The sub-airgap is defined as the yap between the sides of the clawpoles of the two separated pieces.

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For continuous rotation, either the stator cores or themagnets should be shifted through an angle betweenphases. In the case of this three-phase three-stack clawpole motor, the shift between different stacks is 120'electrical, while the magnets with the same polarity arelined up.

IV. 3D MAGNETIC FIELD ANALYSISFinite element analysis has been recognized as asuitable and accurate method of field computation to aidmotor design, allowing material non-linearity . andstructure details to be included.Because of the complex geometry, the magnetic fieldin a claw pole motor is truly three-dimensional. In 3D fluxmachines, the armature carries significant field in all threedirections. This is only achievable using SMC material.Consequently, for the correct calculation of magnetic fieldand motor characteristics, a 3D numerical analysis isrequired.By taking the advantage of the periodical symmetry,only one pole pitch of the machine needs to be studied. Atthe two radial boundary planes, the magnetic scalarpotential used to solve the magnetic field distributionobeys the so-called half-periodical boundary conditions:qmY,Ae I 2, z )=-qm r,-Ae 1 2 7 2 ) (1)

where cylindrical coordinates are used and de=18" is theangle of one pole pitch.A number of key parameters of the motor can bedetermined from the numerical magnetic field analysis[7]. The no-load magnetic field distribution is calculatedto find out the magnetic flux linking the stator winding.The motor structure and dimensions were adjusted suchthat the flux linkage was maximum. The inducedelectromotive force ( em j ) under rotation is inferred bydifferentiating the no-load flux with respect to e. For theclaw pole motor the em f was found to be closelysinusoidal.Cogging torque arises from the reluctance variation ofthe magnetic circuit as the rotor rotates and exists evenwhen there is no stator current. The cogging torque can becomputed by the virtual work or Maxwell stress tensormethods after the magnetic field distribution isdetermined. The cogging torque has a period of 180"electrical and is anti-symmetric about zero, and hence hasonly even sine harmonics. As the stator stacks are shiftedby 120" electrical, the torque harmonics of the threestacks sum to zero except for the 6'h order and itsmultiples.The self-inductance of each phase winding can becalculated by Ll=Nlq51111,where is the magnitude of theflux linking the stator winding due to a stator current I , ineach of N I turns. It can be obtained from the results of afield analysis with a stator current I , while the permanentmagnets are "switched off ', i.e. remanence is set to zero.

The armature reaction at the rated current can also becomputed by this field analysis to check whether themagnets would be demagnetized.An improved method is applied for predicting thecore losses of this 3D-flux SMC motor [SI. Differentformulations are used for core loss prediction withalternating, circular rotating, and elliptically rotating fluxdensity vectors, respectively. A series of 3D finiteelement analyses are conducted to determine the fluxdensity locus in each element when the rotor rotates. Thecalculated no load core loss, varied approximately linearlywith frequency and was 58 W at 300 Hz. Under the ratedload it will increase by about 20%.

v. S E N S OR L E S S RUSHLESS DC DRIVEThe claw pole SMC PM motor prototype has beendriven by a six-step 120" rotor position sensorlessbrushless DC motor controller. Fig.2 sketches the inverterpower circuit, featuring it 3-phase MOSFET bridge.The DC rail voltage:; are assumed to be +VD& and -

VD&. For six-step 120" switching a half cycle of anyphase voltage is as follows: connection to one of the DCrails for two of the six steps, i.e. for 120"; followed by onestep of 60" comprising two parts, a commutation periodwhen the phase current decays to zero while connectedvia the freewheeling diode to the other DC rail, and afloating period, when the phase is disconnected and thephase current is zero. 'Note that it is assumed that thecurrent at the start of the commutation period has thesame sign as the DC rail to which it has been connected.If it has the opposite sign then the other diode would keepit connected to the same DC rail during commutation.

VI. PERFOIRMANCE ANALYSISWhen the motor is operated in brushless DC mode,the three phase voltages are controlled according to therotor position such that fundamental components of thephase current I1 and the induced emJ El are in phase, toachieve a maximum electromagnetic power P,,, at a givenspeed, i.e.

e,,, 3E , I ,

3 1

Fig. 2. Inverter power circuit

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The induced rm s line-neutral stator emf can bedetermined by

(3)where w1=2@, is the angular rotor speed in electricalradians per second,1;he frequency of the induced statoremfin Hertz, N I he number of turns of the stator winding,and $ the magnitude of the magnetic flux linking thestator winding due to the permanent magnets.From the no-load magnetic field analysis, the curvesof the stator flux and the induced emjversus rotor angle ortime are almost sinusoidal. The back emf's for three phasewindings are taken as

where the switching is assumed to occur at 0 = wlt =0,and 0, is the advance of the switching angle ahead of theback emf: Bidirectional motors with a single set ofposition sensors must have 0, 0, but a slight advance isneeded for alignment of back-emf and current as requiredfor minimum copper loss [9].To obtain the currents in three phases the followingequations are to be solved.

(7)(8 )

t,E,. +RI, +L.-L+V, (9 )

Vu = E , +RI, +L-+V,IUdtdtdldt

Vb=Eh+RI,+L-+V,,h

The three phase windings are star connected, so that

The voltage V, at the neutral point can be obtained byaddition of (7 )- 9):

The line-to-neutral rms voltage and phase rms currenthave the following relationship when the motor is with theoptimum brushless DC control:

(300Hz), El= 48.7 V, and for the rated rms current of 4 A,which is limited by the temperature rise of the statorwinding, P,,=585 W and V,=63.7 V. The correspondingDC input voltage of the inverter can be approximatelyestimated by

V,, =2.34V, (13)though this is only accurate for neload [IO].efficiency are calculated byThe output power, output torque, input power, and

where PF, is the core loss, P,,, is the mechanical loss, P,,,is the copper loss, which is assumed here to be dominatedby the fundamental component of current, and I is theangular speed.

VII. PROTOTYPE TESTSFig.3 is a photo which shows the setup for testing the3-phase 3-stack claw pole PM SMC motor (on the right).

A DC machine (on the left) is connected to the prototypemotor via a torque transducer (in the middle). It functionsas the load when the prototype is operated as a motor, orthe driver when the prototype is operated as a generator.A . Resistance Measzrrement

For measurement of the phase winding resistance, afixed DC current of 1A was fed into two of the terminalsof the 3-phase winding. The measured voltage acrossthese terminals was 0.450 V, and therefore the phaseresistance is 0.225 R at the room temperature. The

where RI is the resistance of one phase winding andX I is the reactance. For the prototype motor, at 1800 rpmFig. 3. Set-up of a claw pole PM motor with SMC stator

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resistance at the rated operating temperature rise can becalculated by

4.03.53.02.52.01.5

234.5+ 2R2 = 234.5+ ,

------

where tl is the room temperature, which is 22"C, and tz isthe rated operation temperature 115"C .B. Inductance Measurement

For measurement of the phase winding inductance, anAC current of power frequency was fed into two of theterminals of the 3-phase winding with the rotor lockedand the voltage across the two terminals, 2V1, and thecurrent flowing through the windings, I,, are measured.The inductance of each phase winding can be calculatedby

where f , is the power frequency, viz. 50 Hz. Themeasured average inductance for each phase winding is5.79mH.C. StatorFlux at No Load and emf Constant

The induced open circuit voltage (back emf) wasmeasured by driving the prototype at different speeds, andthe readings are listed in Table 11 The magnet flux wasobtained by (3 ) and the emf constant was by

The stator flux (averaged over three phases) has peak0.488 mw b and the emf constant is 0.259 Vslrad.D. ack emf Waveforms

Fig.4 shows the measured emf waveforms at 1800rpm or 300 Hz., which are very close to sine wave. Asshown, the magnitudes of the three phase emf waveformsare the same but their phase angles are shifted 120"electrical from each other.E. Steady State Characteristics

The steady state characteristics were measured withdifferent loads at a fixed inverter DC link voltage. Theload torque was varied by changing the electrical load ofthe DC generator. Fig.5 illustrates the mechanicalcharacteristics with different fixed DC link voltages. Itcan be seen that the motor speed decreases approximatelylinearly when the load increases.With the rated DC link voltage, 165V, the curves ofinverter input DC current and output AC current againstshaft torque are illustrated in Fig.6, and the variations of

the input power, output power and efficiency are shown inFig.7.Fig.8 shows the waveforms of the stator line voltageswith respect to the average DC rail voltage at the ratedtorque and speed. It can be seen that three voltagewaveforms have the similar shape but shifted by 120electrical degrees. Since the motor speed is 1800 rev/min,the corresponding frequency and period of the applied ACvoltages are 300 Hz and 3.333 ms, respectively. Fig.9

TABLE 11NO LOAD FLUX AN D EM F CONSTANTEMF constantpeed Voltage, L-N Frequency Flux

(rpd (Vl (Hd (mWb) (Vslradl301 8.3 50.2 0.499 0.264597 16.1 99.5 0.487 0.258905 24.5 150.8 0.488 0.2591198 32.3 19!3.7 0.486 0.2581503 40.5 250.5 0.485 0.2571805 48.9 300.8 0.486 0.25990 Line-to-neutralbackEMF (V)

-90

25002000

I5001000

5000

clt (electrical degrees)Fig. 4. Measured back emfwaveform s at 1800 rp m

Speed (revhin)

Torque (Nm)0.0 0.5 Io I .5 2.0 2.5 3.0

Fig. 5 . Speed versus output torque with different DC link voltages4s r lnvertcr

A 1 , , Torque (Nm]0.0 0.5 1o I .5 2.0 2.5 3.00.0 I

Fig. 6. Inverter DC input and AC output currents versus output torque

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plots the waveform of a phase current and its relationshipwith the voltage.The rated performance of 500 W output at 1800 rpmat 80% efficency, from a motor OD 94 mm and totallength (excluding shaft) 137 mm compare favourably withother laminated motors. For example, an aluminum TEFVinduction motor rated 370 W at 1380 rpm, which is aboutthe same torque (3% lower), has efficiency only 73%from frame size D71G, with OD 126 mm including finsand total length 220 mm (including fan but excludingshaft) [l I]. Or as a second comparison - lower torquebut higher power (610 W) brushless DC servo motor,

700600500400300200100

504030out

0 1 00.0 0. 5 1.0 1.5 2.0 2. 5 3.0

Output torquc (Nm)Fig. 7. Curves of inverter input power, motor output power and systemefficiency versus output torque

-100 1 ITimc (ins)Fig. 8. Three phase waveforms of the line AC voltage with respect to theaverage DC rail voltage at 1800 rpm

Time (ms)Fig. 9. Phase voltage and current waveforms

rated 2.2 Nm locked rotor and 1.95 Nm at 300 rpm (whenmounted to a cooled 25C flange), hss square cross-section 100 mm and length 173 mm [12]. The claw poleSM C motor has similar performance from a smallervolume compared to these commercial motors.

VIII. CON CLUSIO N AND DISCUSSIONTo investigate the potential of SM C materials inmanufacturing small motors of complex structures, a 3-phase PM claw pole motor with SM C core has beendesigned and manufactured. The prototype is operatedwith a sensorless brushless DC drive and its performanceis comparable to that of similar motors with electricalsteel cores at potentially reduced manufacturing cost. Themethod for the motor design and performance analysishas been validated by experiment.

ACKNOWLEDGMENTThe authors wish to thank Hoganas AB , Sweden, forsupplying preforms of SOMALOFM500.

REFERENCES[I] A.G. Jack, Experience with the use of soft magneticcomposites in electrical machines, in Pruc. Inr. Con6 onElectrical Machines, Istanbul, Turkey, 1998, pp. 1441-1448.P. Jansson and A. Jack, Magmetic assessment of SMCmaterials, in Proc. 21 Annua l Conf: on Properries andApplicat ions of Magnetic Materials, Chicago, May 2002, pp.

T.J. Hammons, H.B. Ertan, J.A. Tegopoulos, W. Drury, M .Ehsani, T. Nakata, and A.G. Jack, 1998 ICEM review,IEEE Power EngineeringReview, Feb. 1999, pp. 12-17.Soft magnetic composites from Hiiganls metal powders -SOMALOYTM 500 , Cata logp SMC 01, Hoganas AB,Sweden.[5] RM-core non-oriented magnetic steel sheet and strip,Catalogue, Kawasaki Steel, Mar. 1999.

[6] Y. G. Guo, J. G .Zhu, P. A. Watterson, and W., Wu, Designand analysis of a transverse flux machine with sot\ magneticcomposite core, The 6 Int. Con t on Electrical MachinesandSysrems,Beijing, China, Nov. 2003.Y. . Guo, J. G . Zhu, P. A. Watterson, and W. W u, Designand analysis of a three-phase three-stack claw pole permanentmagnet motor with SMC stator, Aiistralusian UniversitiesPower Eng. Cont . Christchurch, New Zealand, 28 Sept. - 3Oct . 2003.Y. . Guo, J. G. Zhu, J. J. Zhong, and W. Wu, Core losses inclaw pole permanent magnet machines with soft magneticcomposite stators, IEEE Trans. M a p . , vol. 39, no. 5, Sept.2003.P.A. Watterson, Phasor analysis of six-step 120 conductionpermanent magnet motor drives, 2 Int. Con$ on PowerE1ectronic.s Drives and Energy systems, Perth, Australia, 30Nov. - Dec. 1998.[IO] P. A . Watterson, Analysis of six-step 120 conductionpermanent magnet drives, Acc.stmlasian Universities PowerEng. ConJ. Sydney, 28 Sept. - 1 Oct. 1997, pp. 13-18.

[ I I] Aluminum IP54 m otors, Brook Crompton CataloguelX180 0, July 1991.[121 FAS T series brushless servomotors, Vickers CatalogueEPC-GB-B-4030, Motor FA S TI M2 030,1991.

[2]

1-9.[3]

[4]

[7]

[8]

[9]

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T h e 2 0 0 3 In te rn a ti o n a l C o n f e r e n c e o nP o w e r E le c t r o n i c s a n d D r i v e S v s t e m s

P E D S 2 0 0 3

~

PEDS

11 - 20 N o v em b e r 20 03N o v o t e l A p o l l o H o t e l

S in g a p o r e

Edited by

King-J et Tseng

Organised byIndustry Applications / Power Electronics J oint Chapter of IEEE Singapore

Section

+IEEE

In Technical Co-sponsorship withIEEE Industry Applications Society

IAS~e

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2003 IEEE. Personal use of this material is permitted. However,

permission to print/republish this material for advertising or promotionalpurposes or for creating new collective works for resale or redistribution

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M es s ag e f r o m t h e O rg an i z in g C h a i rm an

On behalf of the PE DS'03 Organizing Committee, it is a great honor for me to extend a warm

welcome to all the participants taking part in the Fifth IEEE International Conference on

Power Electronics and Drive Systems (PEDS). The PEDS Conference originated in

Singapore and the first PEDS conference was held in Singapore in 1995. The aim of the

PEDS Conference is to provide a forum for participants from the industry and academia in the

area of power electronics and drives to exchange ideas and have interactions. The

conference is biennial and since 1995 the PEDS Central Committee, Singapore in

collaboration with overseas organizing committees have organized four such conferences

(PEDS-95 Singapore, PEDS-97 Singapore, PEDS-99 Hong Kong and PEDS-01 Bali). All the

PEDS conferences are being held in technical co-sponsorship with the IEEE Power

Electronics Society and IEEE Industry Applications Society.

After a gap of nearly six years, PEDS has now comeback to Singapore. The conference

includes a half-day tutorial type of four technical seminars to be provided by eminent

researchers in the afternoon of 17th

November 2003, followed by three days of technical

paper presentations from i s " - z o " November 2003. The Technical Program Committee has

assembled a program that is outstanding in quality and diversity. There will be 322 technical

papers presented during the conference, involving authors from 36 different countries.

Besides the technical program spreading over four days, there are many exciting tourist

attractions within Singapore as well as in the S outh East Asian region for the delegates to

explore. I hope the conference delegates would bring their families along to enjoy these

attractions during the pre/post-conference period. We have appointed a travel agent who

would be located at the conference site to provide help to conference participants and their

families.

Finally, I would like to thank everybody involved in the organization of this event for having

brought together an outstanding technical program and wish all the participants a very

successful conference with fruitful discussions and enjoyable stay in Singapore.

Sanjib Kumar Panda

PEDS 2003 Organizing Chairman

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M es s ag e f r o m t h e T ec h n i c a l P r o g ram C h a i rm an

This Fifth IEEE International Conference on Power Electronics and Drive Systems (PEDS

2003) has broken a number of its own records. It received an overwhelming response of 413

digests submitted to its Technical Program Committee. After the review process by the 66

members of the Technical Program Committee, 322 papers are finally included in the

conference proceedings, which is another record. These papers coming from a record of 36

countries will be presented in 25 oral sessions and 4 poster sessions over the 3-day

conference. The introduction of poster presentations is another new development in this

PEDS conference.

In keeping with tradition, the conference would be preceded by professional seminars on 17

Nov 2003. There will be a keynote address by Prof Akagi on "Trends in Power Electronics

and Motor Drives" during the opening ceremony on the morning of 18 Nov 2003, followed by

a plenary session of 4 very interesting papers. Another new feature in this PE DS conference

is the Rap Session in the evening of 18 Nov 2003, where a panel of distinguished power

electronic experts will lead a light-hearted discussion with the audience on a thought

provoking topic.

As power electronics and drives technologies mature, there is increasing focus on applicationissues. Hence the Technical Program Committee has adopted the theme of "Emerging

Opportunities for Power Communities" for P EDS 2003. This is reflected in the applications-

oriented arrangement in the technical sessions. I hope our delegates can depart from this

PEDS conference with new application ideas and new friendships to seek new opportunities

in their areas of specialization.

Finally, I would like to express my sincere appreciation to all the members of the Technical

Program Committee for their timely and outstanding efforts in reviewing the large number of

extended digests. I wish all delegates an enjoyable time in this conference.

King-Jet Tseng

PEDS 2003 Technical Program Chairman

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LS3.4 Permanent Magnet Motor Drives

Date:

Time:

Venue:

Co-Chair 1:

Co-Chair 2:

19 Nov 2003, Wednesday

14:00

Venus 1

Dr David Dorrell

Prof Mahinda Vilathgamuwa

LS3.4-01 OPTIMIZED DESIGN OF PMSM INNER POTENTIAL WAVEFORM FOR

LOW-SPEED & HIGH-TORQUE DRIVE SYSTEM 671

BY Zhang, GG Sun, GH Feng, YF Zeng, and LF Wang: Shenyang University of

Technology, China

LS3.4-02 FINITE ELEMENT CALCULATION THE SATURATION DQ-AXES

INDUCTANCE FOR A DIRECT-DRIVE PM SYNCHRONOUS

MOTOR CONSIDERING CROSS-MAGNETIZATION 677JH Hu, JB Zou and WY Liang: Harbin Institute of Technology, China

LS3.4-03 QUANTITATIVELY EVALUATION THE NONIDEAL COGGING

TORQUE OF PERMANENT MAGNET MOTOR CAUSED BY

STATOR AND ROTOR DEFECT 682

J B Zou, JH Hu and WY Liang: Harbin Institute of Technology, China

LS3.4-04 AN EXTENDED KALMAN FILTER OBSERVER FOR THE DIRECT

TORQUE CONTROLLED INTERIOR PERMANENT MAGNET

SYNCHRONOUS MOTOR DRIVE 686

Z Xu and MF Rahman: University of New South Wales, Australia

LS3.4-05 A SPACE VECTOR MODULATION DIRECT TORQUE CONTROL FOR

PERMANENT MAGNET SYNCHRONOUS MOTOR DRIVE SYSTEMS 692

o Sun and J G Zhu: University of Technology, AustraliaYK He: Zhejiang University, China

LS3.4-06 VARIABLE PARAMETER PI CONTROL OF A NOVEL DOUBLY

SALIENT PERMANENT MAGNET MOTOR DRIVE 698

M Cheng and Q Sun: Southeast University, China

LS3.4-07 IMPROVED DESIGN AND PERFORMANCE ANALYSIS OF A CLAW

POLE PERMANENT MAGNET SMC MOTOR WITH SENSORLESS

BRUSH LESS DC DRIVE 704

YG Guo, J G Zhu, PA Watterson and WM Holliday: University of Technology,

Australia

W Wu: CSIRO Telecommunications and Industrial Physics, Australia

LS3.4-08 DISTRIBUTED CONTROL OF PERMANENT MAGNET SYNCHRONOUS

MOTOR DRIVE SYSTEMS 710

L Samaranayake and YK Chin: Royal Institute of Technology, Sweden

USK Alahakoon: University of Peradeniya, Sri Lanka

LS3.4-09 ADAPTIVE TARGET POSITIONING CONTROL FOR PERMANENT-

MAGNET SYNCHRONOUS MOTORS WITH LOW-RESOLUTION

SHAFT ENCODER 716

KY Cheng, CT Yao and YY Tzou: National Chiao Tung University, Taiwan

LS3.4-10 SENSORLESS SLIDING MODE CONTROL OF AN INTERIOR

PERMANENT MAGNET SYNCHRONOUS MOTOR BASED ON

EXTENDED KALMAN FILTER 722

Z Xu and MF Rahman: University of New South Wales, Australia