刀桿式手動壓機設(shè)計(1)帶CAD圖,刀桿式,手動,設(shè)計,CAD 806IEEE TRANSACTIONS ON INDUSTRY APPLICATIONS, VOL. 40, NO. 3, MAY/JUNE 2004MechanicalDesignConsiderationsforConventionallyLaminated, High-Speed, Interior PM SynchronousMachine RotorsEdward C. Lovelace, Member, IEEE, Thomas M. Jahns, Fellow, IEEE, Thomas A. Keim, Member, IEEE, andJeffrey H. Lang, Fellow, IEEEAbstractThis paper discusses mechanical design consid-erations that are particular to conventionally (i.e., radially)laminated rotors of interior permanent-magnet synchronousmachines. Focus is placed on applications where the radial forcesdue to high-speed operation are the major mechanically limitingdesign factor. Proper design of the lamination bridges, or ribs,at the rotor outer diameter is explained in terms of the bothmaterial considerations and electromagnetic performance impact.The tradeoff of complexity versus performance associated withusing strengthening ribs in the magnet cavities is discussed. Thesensitivity of the mechanical design limitations to the rotor-shaftmounting mechanism is also highlighted. These effects are thenanalyzed using finite-element analysis for a 150-N m/6-kWintegrated starter/alternator designed for operation up to 6000r/min with an annular rotor to accommodate a torque converteror clutch assembly. This example demonstrates that it is possibleto significantly improve the rotors structural integrity using thetechniques described in this paper with only a very modest impacton the projected machine drive cost.Index TermsElectrical steel, finite-element analysis (FEA),highspeed,interiorpermanent-magnet(IPM)synchronousmachine, laminations, magnetic saturation.I. INTRODUCTIONROTOR DESIGN and construction of interior perma-nent-magnet (IPM) machines is a challenging task dueto the conflicting characteristics of improved performance androtor complexity. IPM machines are of interest because they areparticularly attractive from a performance standpoint in tractionandspindle applications1,2.IPMmachinescanbedesignedwith wide, and theoretically infinite, speed ranges for constantpower operation with excellent inverter utilization. This isachieved through use of a salient rotor geometry with limitedPaper IPCSD 03084, presented at the 2001 IEEE International Electric Ma-chines and Drives Conference, Cambridge, MA, June 1720, and approved forpublication in the IEEE TRANSACTIONS ONINDUSTRYAPPLICATIONSby theElectric Machines Committee of the IEEE Industry Applications Society. Man-uscriptsubmittedforreviewNovember5,2002andreleasedforpublicationJan-uary 20, 2004. This work was supported by the MIT Consortium on AdvancedAutomotive Electrical/Electronic Components and Systems.E. C. Lovelace is with SatCon Technology Corporation, Cambridge, MA02142l USA (e-mail: lovelacealum.mit.edu).T. M. Jahns is with the Wisconsin Electric Machines and Power ElectronicsConsortium,DepartmentofElectricalandComputerEngineering,UniversityofWisconsin, Madison, WI 53706-1691 USA (e-mail: jahnsengr.wisc.edu).T. A. Keim and J. H. Lang are with the Laboratory for Electromagneticand Electronic Systems, Department of Electrical Engineering and ComputerScience, Massachusetts Institute of Technology, Cambridge, MA 02139 USA(e-mail: tkeimmit.edu, langmit.edu).Digital Object Identifier 10.1109/TIA.2004.827440flux contribution from PMs buried within the rotor structure.To achieve the desired degree of saliency, special laminationdesign and assembly strategies are typically required comparedto those required for competing machine types such as surfacePM and induction machines.TherotordesignstrategiesforIPMmachinescangenerallybedivided into axially and radially laminated configurations, eachwith its own advantages 3, 4. The axially laminated rotor isconstructed using many alternating layers of soft and hard mag-netic sheets that are laid along the axis of the machine, eachbent and individually sized to form the poles of the rotor 1.This design approach can achieve high-inductance saliency ra-tiosin excess of 10:1. However, the axially laminatedrotorisrelativelyexpensivetomanufactureduetothesortedcut-ting, shaping, and assembly of the many different laminationsthatmustbeemployed. Furthermore, aconstrainingrotorsleevemay be necessary for high-speed operation to prevent lamina-tion intrusions into the air gap. Such sleeves typically reducethe saliency due to their finite thicknesses and often increaselosses due to eddy currents when high-strength stainless steel(e.g., Inconel) is chosen for the sleeve material.By contrast, radially laminated rotors are typically designedwith 14 layers of hard magnetic material in each pole. Eachlamination, as with other conventional machine types, ispunched or cut as a single unitary piece for the cross section ofthe rotor. Cavities are punched or cut into the rotor laminations,and the magnet material is inserted into these cavities. Thelaminations can be stacked using conventional means so thatthe rotor is generally easier to manufacture than its axiallylaminated IPM counterpart.However, adoption of the radially laminated rotor comes atthe expense of saliency with typical inductance ratios rangingfrom 1.5 up to 10:1, depending on the number of magnet cavitylayersand theirconfiguration.Forgoodelectromagneticperfor-mance, it is necessary to minimize thesteel bridges surroundingthe magnetic cavities that are necessary to link the rotor ironsegments into a unitary lamination. Each bridge effectively cre-atesamagneticshortciruitacrossthePMs,therebyreducingthemagnets contribution to the overall air-gap flux.This paper examines the mechanical design issues of con-ventionally (also referred to as transverse or radially) laminatedIPM rotors. Only the centrifugal force is considered as this islikely to be the dominant source of mechanical stress in high-speed designs. Each of several key rotor design features are ex-amined in turn with respect to their influence on the rotor stress0093-9994/04$20.00 2004 IEEELOVELACE et al.: CONVENTIONALLY LAMINATED, HIGH-SPEED, IPM SYNCHRONOUS MACHINE ROTORS807Fig. 1.Cross section of a 12-pole IPM machine.state and electromagnetic performance. Design strategies withrespect to features that can mitigate the resultant mechanicalstress state are also presented. The discussion is substantiatedthrough finite-element analysis (FEA) to verify the arguments.An IPM rotor design for an integrated starter/generator (ISG)application is used throughout the paper to illustrate the signif-icance of these mechanical issues 57. A cross section for a12-pole two-layer design is shown in Fig. 1. In particular, themechanical stress state of this rotor is a limiting design con-straint due to the high rotor tip speed operation that is requiredof annular direct-drive automotive machinery.The pertinent design specifications for this ISG design are: 6000-r/min maximum operating speed; 10000-r/min design burst speed; minimum rotor inner diameter (ID)mm; maximum stator outer diameter (OD)mm; bonded PM material in cavities.II. MECHANICALDESIGN OFIPM ROTORSFor the purpose of this discussion, the mechanical designpoint corresponds to the application specification that producesthe worst case mechanical stress in the IPM rotor. The assump-tions employed in this development are as follows: steady-state speed conditions only; temperature effects neglected; baseline core material: M19 29-gage electrical steel; yield indicated by planar Von Mises stress; forces of electromagnetic origin considered negligible; vibration and rotor shaft dynamical forces neglected.With these assumptions, the forces on the rotor are dominatedby the steady-state centrifugal forces at constant speed. There-fore, the mechanical design point corresponds to steady-stateoperation at the design burst speed value, 10 kr/min.Analytical calculations of the peak stresses due to centrifugalforces acting on a radially laminated IPM machine rotor is achallenging task that is not attempted in this paper due to thecomplexity of the rotor lamination design features. However,these peak stresses affect the boundaries of the optimizationvariables that determine the optimal system design, so a quali-tative discussion of the resultant forces due to inertial loadingis appropriate. The discussion is conducted employing well-Fig. 2.Sketch of resultant forces on a solid rotor.Fig. 3.Sketch of resultant forces on an IPM rotor with one magnet-filledcavity.known principles that describe the behavior of materials understatic loading 8, 9.Fig. 2 shows a solid rotor cross section with annotations toindicate the major forces on the core due to centrifugal loading.At the simplest level, neglecting the magnet cavities, the rotorresemblesahoopwithconstantcentrifugalloading.Undertheseconditions,an elementalmember oftherotor isundertangentialtension and radial compression.Thin-walled hoop approximations can be justified for mod-eling the rotor because of the narrow depth of the ISG rotorin comparison to the rotor ID. As a result, the rotor segmentsmainly experiencetangentialtension forces. Using this assump-tion, the major factors affecting the peak stress are the averageradius of the “hoop” and the rotational speed. The Von Misesstress increases according to the square of each of these factors.If the rotor cavities are now considered as in Fig. 3, whichonly contains one cavity layer, the steel pole piece centered ontheaxis is now only attached to the rest of the laminationby the thin steel bridges at each end. Therefore, the centrifugalloading on the pole piece is not evenly distributed around the808IEEE TRANSACTIONS ON INDUSTRY APPLICATIONS, VOL. 40, NO. 3, MAY/JUNE 2004Fig. 4.Sketch of resultant forces on an IPM rotor with multiple layers.rotor “hoop,” causing a substantially radially directed inertialload on the two retaining bridges.It should be noted that the bonded PM material in the cavitywill also contribute to this loading because it is generally lessstiff than the steel and will, therefore, contribute additionalloading against the inside edge of the pole piece. Therefore,the equivalent magnet mass,in Fig. 3, must be the sum ofboth the steel pole piece and the magnet (the shaded portionof Fig. 3). The bonded magnet material does not provide anysignificant bonding between magnet and steel and, therefore,does not transmit force from the yoke to the pole pieces.The challenge then reduces to modeling the bridges, and thisis largely dependent on the specific bridge shape. If the bridgesare principally straight, then beam bending approximations areappropriate. When multiple layers are considered as in Fig. 4,each layer can be considered as being independently loadedif the inter-cavity steel sections are wide enough to distributeany stress concentrations between adjacent bridges. The loadon each bridge is then the end load in the radial direction due tothe inertial loading on the remaining section of the pole piecebetween the bridge under consideration and theaxis.If the bridges on each layer have the same dimensions, thebridge at the end of the longest cavity will be under the higheststress. If thecavityends are roundedas shown inFig.5, then theeffectivelengthofeach“beam”is reduced,and thesimplebeamapproximations described above are no longer reasonable. Eachtaperedbridgenowresemblesaroundnotchstressconcentrationelement under side loading as shown in Fig. 5.The precise location of the peak stress within each bridgeconfiguration would require significant analysis to determinewithout resorting to numerical solutions. In particular, theequivalent mounting (fixed or simple) at the ends of each“beam” for the straight-bridge model is not clearly defined. Ifthe ends of each bridge experience minimal bending comparedto the rest of the bridge, it is reasonable to assume that the peakstress will be found at the ends. In contrast, the peak stress inthe rounded cavity structural model would be expected at theroot of the stress concentration, corresponding to the midpointof each bridge.Fig. 5.Sketch of resultant forces on an IPM rotor with multiple cavity layerswith rounded tips.At this stage, some general observations can be made aboutIPM rotor design decisions that would worsen or improve themechanical stress conditions. Maximum rotor speedA 10% reduction in the mechan-ical design point speed would reduce the peak Von Misesstress by almost 20%. Rotor ODSimilarly, a 10% reduction in the radius at therotor surface, where the bridges are located, would alsoreduce the stress by a 20% factor. Rounded bridgesThe “beam” stresses are reduced asthe “beam” gets shorter with all other dimensions equal.Based on the characteristics of the notch stress concen-tration model, a circularly rounded bridge shape shouldnearly minimize the peak stress. Smaller pole piecesA 10% reduction of the deflectingpole piece mass per unit axial length will reduce the stressalmost linearly. This can be achievedbyreducingthe frac-tion of the pole pitch that the cavities span. Increasing thenumber of machine poles can produce the same effect. Strengthening ribAdding a rib redistributes the cen-trifugal load from the pole piece resulting in a significantimprovement in the stress state. A rib that is added tothe lamination geometry across theaxis of each cavityresists the centrifugal motion of the pole masses throughtension rather than bending.Another factor in the resultant forces caused by the inertialloading is the effect that the radial deflection of the entire rotorhas on the magnitude of the tensile component of hoop stress.The hoop tension in the bridge is due to stretching as the rotorexpandsinto the air gap at higher speeds. Theimplicit boundaryconditions in hoop stress calculations are that the rotor ID andOD boundaries are unconstrained. As a result, reduction of thedeflection at either boundary will reduce the expansion of therotor at the bridge radius and therefore also reduce the hoopstress component of loading.Constraining the rotor OD is problematic since it would re-quire a material substantially stiffer than steel to decrease theradial deflection under inertial load. Furthermore, adding anyLOVELACE et al.: CONVENTIONALLY LAMINATED, HIGH-SPEED, IPM SYNCHRONOUS MACHINE ROTORS809Fig. 6.Rotor hub design using dovetailed joints between the hub and rotor ID.Fig. 7.Rotor hub design using axial bolts through the stack to an end plate.material in the air gap that adversely affects the electromagneticsaliency of the original rotor would degrade the performance ofthe machine.Constraining the rotor ID is a more feasible solution forimproving the structural integrity of the rotor. Since there isalready a hub that must attach the rotor to the crankshaft, thereis an opportunity to specially design the hub to retain the rotorradially. Typically, a hub is only designed to transmit the torquein the circumferential direction as would occur with a hub thatis press fit inside the rotor. A press fit, though, does nothing toconstrain the rotor ID and so would not mitigate the maximumstress at the mechanical design point.If there are no space constraints inside the rotor ID, a varietyof different hub fixtures might be considered. A welded hubmay work but could alter the magnetic properties of the core.One alternative is an axial cylinder that mates with the rotor IDusingdovetailedsurfacesasshowninFig.6.Anotheralternativeis to construct an end plate with studs distributed around thecircumference of theend plate (oneperpole)as shown inFig.7.The laminations would be cut with a hole along eachaxiswhere the core is widest (i.e., there no cavities along theaxis),and then assembled onto the studs.This bolted system is only practical if sufficient bolt tensioncan be developed and maintained so that the radial load is takenup by the end plate. If adequate bolt tension is not developed,there will be significant side-loading on the studs that wouldlikely result in shearing off the studs at the surface of the endplate.The advantage of the dovetail fixture (Fig. 6) or any fixturealong the rotor ID surface is that it is structurally robust andnearly symmetric if the radial plate portion of the hub is lo-cated axially near the midpoint of the rotor stack. Its chief dis-advantageis that thehubcylinderhas a finitethickness thatmaymake it necessary to reduce the available space for the rotorlaminations.In contrast, the advantage of an endplate structure (Fig. 7) isthat the radial plate is at the end of the stack and does not useany internal real estate inside the ID that might otherwise be re-servedforaclutchortorqueconverter.Asaresult,thisapproachmay yield the most compact ISG configuration. Furthermore,the absence of the internal hub allows the rotor to be designedwith the smallest possible ID and OD, which will reduce thepeak stress (squared impact on stress). However, any endplateapproach must solve the practical installation problems associ-ated with heavily loaded studs and compressed laminations.In Section III, the endplate hub structure is analyzed incombination with proposed rotor cross-section modifications todemonstrate a plausible solution for the mechanical design ofan IPM machine for the ISG application. The endplate design ischosen for analysis because it allows the smallest machine rotordiameter consistent with the given ISG constraint to providespace inside the rotor ID for a torque converter.The mechanical design considerations discussed above affectthe design performance optimization of IPM machines in sev-eral ways 6, 7, 10. RotordiameterConstrainingtherotordiameterandpolepiece sizes clearly reduces the available design space foroptimization. Rotor materialThe choice of rotor lamination materialaffects allowable stress state based on the material yieldstrength, butit alsoaffectsthecorelosses 1114.Sincethe fundamental rotor field is dc, though, the core lossesare substantially confined to harmonics introduced by thelamination geometry. The rotor material also influencesthe required magnet strength for a given PM flux-linkagedesign because the choice of alloying material contentalters the saturation flux density. The saturation flux den-sity, in turn, affects the proportion of the magnet flux thatis shorted through the bridges and strengthening ribs. Bridge and rib geometryThe geometry of the bridgesand strengthening ribs directly affects magnetic perfor-mance. For a given IPM machine design, changing fromstraight to curved cavity tips with the same minimumbridge/rib width increases the flux that is shunted throughthe bridges and ribs. Adding additional strengthening ribsalso increases the proportion of shunted magnet flux. Allthese bridge and rib factors serve to reduce the availableair-gap flux from the permanent magnets, thereby re-ducing the magnet torque component for a given designor requiring the introduction of larger, stronger magnets.810IEEE TRANSACTIONS ON INDUSTRY APPLICATIONS, VOL. 40, NO. 3, MAY/JUNE 2004Fig. 8.Radial displacement with straight-edge bridges at 10 kr/min.For a given design that was initially optimal from an inverterutilization standpoint (i.e.,) 1, design changessubsequently introduced for mechanical reasons shift themachine design point away from the electromagnetic optimum.Ultimately, these changes typically manifest themselves as costand/or size increases for the machineinverter combinationcompared to their comparable values when the machine isoptimized for electromagnetic performance alone.III. FEAOF ANIPM ROTORDESIGNStructural FEA was conducted to confirm the qualitative un-derstandings presented above 15. These results are also usedas a baseline for scaling to other IPM machine designs pro-vided that the dimensional differences with the baseline are suf-ficiently small. The FEA was carried out using the ANSYS 2Dsoftware package.Fig. 8 shows the predicted radial displacement of a double-layer IPM machine at 10 kr/min without considering any rotorID deflection constraint due to an attached hub (i.e., a free rotorID boundary). This cross section is from an ISG with 12 polesand a roto