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22
Investigation of Turn-To-Turn Closures of Stator Windings to Improve the Diagnostics System for Induction Motors
Gubarevych O., Goolak S., Daki O., Tryshyn V.
State University of Infrastructure and Technologies Kyiv, Ukraine
Abstract. The efficiency of using three-phase asynchronous electric motors with a squirrel-cage rotor in the transport sector depends on increasing the level of their reliability, which is possible due to the constant improvement of existing and the development of new diagnostic methods of high reliability. The most labor-consuming and difficult is the possibility of diagnostics and differentiation of turn-to-turn closures of the stator winding. The aim of the work is to establish the nature of the manifestation, influence on energy indicators and determine the diagnostic parameters of turn-to-turn closures on one and simultaneously on two phases of the stator winding of an induction motor using mathematical modeling methods. This goal was achieved through a set of studies using a refined mathematical model of an asynchronous motor, which allows you to create asymmetry of the stator windings, simulate turn-to-turn connections on one phase and simultaneously on two phases in various combinations. The most significant result of the work is the establishment of the dependences of the pulsations of the electromagnetic moment, the unbalance coefficient of the stator phase currents and the energy characteristics from the turn-to-turn short-circuits of the phases of the stator windings. The significance of the results obtained consists in establishing the dependences of the manifestation of various types of damage to the phases of the stator winding necessary for choosing a method for diagnosing turn-to-turn faults in the stator windings when building an effective diagnostic system for asynchronous motors as part of transport infrastructure drives.
Keywords: transport infrastructure, diagnostics, asynchronous motor, mathematical modeling, turn-to-turn circuit, phase, winding, stator, ripple, torque. DOI: https://doi.org/10.52254/1857-0070.2021.2-50.02 UDC: 621.313.333.2
Investigarea scurtcircuitelor între spine ale rnfâsurârilor statorice cu scopul perfectionarea sistemelor de
diagnosticare a motoarelor cu inductie Gubarevici O.V., Gulac S.A., Dachi E.A., Trisin V.V.
Universitatea de Stat a Infrastructurei si tehnologiilor Kyev, Ucraina
Rezumat. Motoarele asincrone trifazate cu colivie de veveritâ sunt unele dintre cele mai comune tipuri de masini electrice utilizate în sectoral transporturilor. Eficienta utilizârii acestor motoare electrice depinde de cresterea nivelului de fiabilitate a acestora, ceea ce este posibil datoritâ îmbunâtâtirii permanente a metodelor existente si dezvoltârii de noi metode de diagnosticare cu fiabilitate înaltâ. Scopul lucrârii este de a stabili natura manifestârii, influenta asupra indicatorilor energetici si de a determina parametri de diagnosticare a scurtcircuitelor între spine unei fazei si simultan pe douâ faze ale înfâsurârii statorice a motoarelor asincrone ale mecanismelor de transport folosând metodele de modelarea matematicâ. Acest obiectiv a fost realizat prin efectuarea unui set de studii asupra modelul matematic rafinat al motorului de inductie, care face posibilâ crearea asimetriei înfâsurârilor statorului, simulând scurtcircuit între spine pe o singurâ fazâ si simultan pe douâ faze în diferite combinatii. Simularea a fost efectuatâ pentru un stator nedeteriorat, apoi la simularea închiderii virajelor, mai întâi doar pe o fazâ si apoi închiderea simultanâ pe douâ faze ale înfâsurârii statorului în diferite combinatii. Cel mai semnificativ rezultat al lucrârii este stabilirea dependentelor de pulsatii ale momentului electromagnetic, coeficientul de dezechilibru al curentilor de fazâ statorici si caracteristicile energetice de la scurtcircuitelor între spine ale înfâsurârilor statorului.
Semnificatia rezultatelor obtinute constâ în stabilirea dependentelor de manifestare a diferitelor tipuri de deteriorare a fazelor înfâsurârii statorului, care sunt necesare pentru alegerea unei metode pentru diagnosticarea defectiunilor spinelor în înfâsurârile statorului atunci când se construieste un sistem eficient de diagnosticare pentru motoare asincrone ca parte a unitâtilor de infrastructurâ de transport.
Cuvinte-cheie: infrastructurâ de transport, diagnosticare, motor asincron, modelare matematicâ, scurtcircuit între spine, fazâ, înfâsurare, stator, ondulare, cuplu.
© Gubarevych O., Goolak S., Daki O., Tryshyn V. 2021
Исследование межвитковых замыканий обмоток статора для усовершенствования систем диагностики асинхронных двигателей Губаревич О.В., Гулак С.А., Даки Е.А., Тришин В.В.
Государственный университет инфраструктуры и технологий Киев, Украина
Аннотация. Трехфазные асинхронные двигатели с короткозамкнутым ротором являются одними из наиболее распространенных типов электрических машин, применяемых в транспортной сфере. Эффективность использования этих электродвигателей зависит от повышения уровня их надежности, что возможно за счет постоянного усовершенствования существующих и разработки новых диагностических методов высокой достоверности. Наиболее трудоемким и сложным остается возможность диагностики и дифференцирования межвитковых замыканий обмотки статора. Целью работы является установление характера замыкания, влияния его на энергетические показатели двигателя и определение диагностических параметров межвитковых замыканий на одной и одновременно на двух фазах обмотки статора асинхронных двигателей транспортных механизмов с использованием методов математического моделирования. Поставленная цель была достигнута за счет проведения комплекса исследований на уточненной математической модели асинхронного двигателя, позволяющей создавать несимметричность обмоток статора, имитирующую межвитковые замыкания на одной фазе и одновременно на двух фазах в различных комбинациях. В качестве объекта исследований использован асинхронный двигатель с короткозамкнутым ротором мощностью 11,0 кВт с известными паспортными параметрами. Методика проведения исследований включает изучение влияния различных видов межвитковых замыканий на электрические, механические и энергетические показатели. Моделирование проводилось для неповрежденного статора, затем при имитации замыкания витков сначала только на одной фазе и затем одновременного замыкания на двух фазах обмотки статора в различных комбинациях. Наиболее существенным результатом работы является установление зависимостей пульсаций электромагнитного момента, коэффициента небаланса фазных токов статора и энергетических характеристик от межвитковых замыканий фаз обмоток статора. Значимость полученных результатов состоит в установлении зависимостей проявления различных видов повреждений фаз обмотки статора, необходимых для выбора метода диагностики межвитковых замыканий в обмотках статора при построении эффективной диагностической системы асинхронных двигателей в составе приводов транспортной инфраструктуры.
Ключевые слова: транспортная инфраструктура, диагностика, асинхронный двигатель, математическое моделирование, межвитковое замыкание, фаза, обмотка, статор, пульсации, момент.
INTRODUCTION
In order to ensure the efficient operation of the transport system it is necessary to improve its reliability. This requires its permanent development and perfection of the diagnostic methods and systems of the operative control in the current-state evaluation and prediction the period of unfailing service [1].
As the drive motors for the railway vehicles and auxiliary equipment both for the railway and water transport the asynchronous motors with a with a squirrel-cage rotor are extensively used.
The fault analysis of the asynchronous motors [2,3] showed that about 15 % of the total amount of this motor type failures occurs because of the inter-turn short-circuits in the stator phase windings. Hence, the complex approach to the study of the processes arising in the asynchronous motor at the inter-turn short-circuit are of primary importance to diagnose the faults of the kind.
The inter-turn short-circuits failure is the type of a fault that is most hard to be diagnosed. It leads to temperature rise in closed sites [4, 5],
which ruins the insulation [6] and creates the drive emergency failures at the drive's long-term service [7].
In addition, the diagnosis complexity of the inter-turn short-circuits of the stator winding is increased by the fact that the external features of the defect can be similar to those of a number of other faults [8].
In this case, the creation of a more authentic diagnostic system necessitates a still further study of the consequences, which result from the stator windings faults, the creation of scientific bases according to the researches carried out and the prime items development of the integrated complex for reliability improvement of the transport infrastructure.
The researches of [9] showed that the analysis of arising the inter-turn short-circuit faults of different degree at a single phase of the stator winding of the asynchronous motor, exhibited the origin of substantial torque pulsations of the motor and asymmetry of stator phase currents. The torque pulsations are observed mainly in the idle-run mode. In addition, the fault of this kind
increases the consumed power, decreases the emf and the motor power factor, reducing thus the motor energy indices.
The kind of failure of the asynchronous motor stator as the inter-turn short-circuit simultaneously on both stator windings, in practice can be met much scarcer, than on a single winding, however, it also needs a thorough study. To build up an efficient system of diagnostics you need first to select a diagnosis method and a method for the following development of the block of identification and differentiation of the failure. In its turn, the choice of the diagnosis method is based on the character of changes in the motor parameters at the occurrence of the inter-turn short circuit in the stator winding.
From the analysis of the effect of the turn-to-turn short-circuit at a single stator phase on the characteristics of the asynchronous motor with a squirrel-cage rotor [10, 11] it follows that:
- the inter-turn short-circuit at a single stator phase increases the current in the faulted phase, which increases the average current of the stator, thus, enlarging the active power losses;
- the inter-turn short-circuit at the stator single phase increases the motor electromagnetic torque pulsations, which are mainly developed in the idle-run mode;
- the inter-turn short-circuit at the stator single phase increases the imbalance of the stator phase currents and, hence, leads to asymmetry of the stator rotating field.
It follows from the aforementioned that to detect, identify and differentiate the failure in question the thermal, electric, vibration and combined diagnosis methods can be used.
The thermal methods application are described in [4, 12]. These methods are based on the heating temperature increase of the stator faulted phase winding under the inter-turn short-circuit, which is the result of the increase in the current average value of this phase. However, the use of these methods is complex at identification and authentic differentiation of the type and degree of the stator winding failure, and, what is more, at the faultless time prediction of the electric motor operation.
The use of the diagnosis vibration methods [13, 14] make it possible to reveal the presence of failures in the stator winding according to the spectra of the vibration signals. The vibro-signal parameters enable to determine the presence of a number of failures as well by means of special sensors. However, for the control, precise
identification of the defect detected, its development and prediction of the residual resource, a base of the vibration signals typical for various kinds and degrees of a fault of the stator winding is necessary. In addition, for the diagnostic systems in the drive configuration, the difficulty of the use of these methods is also in that the estimation of the torque pulsation in the presence of the failures of the stator winding develops mainly with the vibration diagnosis used in the idle-run mode [9], whereas the drive always works under the load.
The diagnostic electrical methods used for the practical issues are based on comparison of the values of the starter phase currents of the motor in its operating and faulted conditions. Thus, [15] compares the spectra of the starter currents of the operating motor and that with the stator winding failures. The spectra of the stator phase currents are studied [16, 17] in the steady condition for the operating motor and for the motor with the wavelet transforms of the stator phase currents in the steady mode for the operating motor and the faulted motor are presented [18, 19]. The finite element method was applied to study the changes in magnetic fluxes of the faulted and operating motor conditions [20]. The failure diagnosis of the stator winding is offered to be performed by way of comparison of these fluxes.
To estimate the degree of failure of the stator winding the modern techniques can be used [21], in which the decision block is realized using the neuron networks. Also the decision block can be realized by the use of mathematics of indistinct logics [22]. In addition, to apply the decision block it is necessary to have the data on the character of the change of a particular parameter and their effect on the motor efficiency.
To develop the diagnostic system with an authentic decision for the determination of a different kind and degree of a stator winding failure, a thorough research must be performed and the character of manifestation and modifying the parameters occurring upon the inter-turn short-circuit simultaneously on two phases of the stator winding must be studied. This phenomenon may also happen in the operational process of the asynchronous motor.
In this work, the complex approach is offered for the study of the effect of the inter-turn short circuit simultaneously on two phases of the asynchronous motor stator. The approach consists of performing the analysis of the influence and establishing the regularities of this
defect on the parameters and characteristics of the motor and of comparison of the order of modification of the characteristics and parameters, depending on the combination degree of the inter-turn short-circuit in two phases of the windings. In [23] it is shown that the asynchronous motor integrated into various technological drives is fed from the nonsinusoidal nonsymmetric system of voltages. Power supply from the voltage system of such a kind induces the torque pulsation on the motor shaft. In this context, during this research the admissions are accepted on the supply system quality of the asynchronous motor, which is considered strictly symmetric, whereas the form of the voltages is sinusoidal.
The results of this work can be used for selection of the efficient method for plotting the diagnostic schemes of asynchronous motors with a squirrel-cage rotor and creation of the diagnostic complex as part of the transport drive.
The aim of this study is to establish the manifestation character, the effect on the power indices and the diagnostic parameters' determination of the inter-turn short circuits at a single and, simultaneously, at two phases of the stator windings of the asynchronous motor, using the methods for the mathematic modeling.
MATHEMATIC MODEL CHOICE FOR
THE PROCESSES' RESEARCH IN ASYNCHRONOUS MOTOR UPON THE INTER-TURN SHORT-CIRCUITS
The asynchronous motor with a squirrel-cage rotor (an AIR132M4 11,0 kW model (Table 1)) was selected as the object for the research.
Selecting a model to study the inter-turn short circuits in the phases of the asynchronous motor stator winding, the possibility must be considered of creation nonsymmetrical fields in it, which takes place upon this failure, In [24, 25], the model is considered, in which the equations that describe the asynchronous motor operation, are written in a single-phase coordinate system. However, the use of this model makes it difficult to define certain parameters, particularly, the unbalance factor of the phase currents.
In the research of the inter-turn short-circuit in a single phase of the stator winding [9], the model is used (Goolak S., Gubarevych O., Yermolenko, E, Slobodyanyuk M, Gorobchenko, O. https://doi.org/10.15587/1729-
4061.2020.199559), in which the nonsymmetry effect on characteristics like the inductance of the magnetization circuit and mutual inductance are taken into account according to the techniques, which is described in (Goolak S., Gerlici J., Tkachenko V., Sapronova S., Lack T., Kravchenko K.
https://doi.org/10.26552/com.C.2019.2.24-31).
The work presented did not consider the phenomena such as the magnetic system saturation and rotor current displacement, which affect the dynamic of the model and the losses. However, they do not affect substantially the preset problem concerning the stator winding diagnostics.
Table 1.
Rating of asynchronous motor with a squirrel-cage rotor AIR 132M4
Parameter Designation Unit of measure Value
Nominal power on the shaft Pn kW 11.0
Nominal phase voltage Un Volt 220
Nominal frequency of feeding voltage fn Hz 50
Frequency of rotor spinning in idle-run mode nn.idle rot/min 1498
Load moment of idle run Tidle Hm 0.38
Active resistance of stator winding ri Ohm 0.5
Active resistance of rotor winding, reduced to stator winding r'2 Ohm 0.36
Reactive resistance of stator winding Xi Ohm 0.56
Frequency of rotor spinning in nominal mode nn rot/min 1450
Motor shaft torque moment Tn Hm 72,671
Motor momentum of inertia J kg-m2 0.04
The accepted simulation model of an asynchronous motor with a squirrel-cage rotor is written in the "braked coordinates".
The systems of control that describe the motor operation look like as follows
u = r ■ i + dw / dt;
sa sa sa t sa '
u „ = r„ ■ i„ + dw „ / dt;
sp sp sp T sp '
u = r ■ i + dw / dt;
sy sy sy T sy '
■ ,dWa ,( Wrp - Wry )■ P ■ ®r
dt
73 ' (1)
Uo - r n ■ i r, ~+
rp rp rp
dWp ( Wry - Wra )■ P-
dt
73
. dyn ( Wra - Wrp )■ P--u = r ■ Z +-'- + ---
n n n dt 73
where u is the voltage, V; i is the current, A; t is time, s; r is the resistance, Ohm; y is the flux linkage, Wb; p is the number of pole pairs. Indices of a, P, y designate belonging to a certain phase; lower index 5 is belonging to the stator phase; lower index r is belonging to rotor phase; and ®r is the rotor spinning frequency rad/s.
The flux linkages are described using the following system of differential equations
Vsa = Lsa ■ isa - ^ 5 ■ M ■ ^ - 0, 5 ■ M ■ ^ +
+M ■ (ira - 0,5 ■ i„ - 0,5 ■ in ) ;
Wsp = Lsp ■ ZsP - 0 5 ■ M ■ isa - 0 5 ■ M ■ +
+M ■(i. - 0,5 ■ i - 0,5 ■ i );
\rp > ra > ryy Wsr, = ■ i„ - 0, 5 ■M ■ isa - 0, 5 ■ M ■ ZsP +
+M ■( in - 0,5 ■ ira - 0,5 ■ irp ) ; w = L ■ i -0,5■M■ in -0,5■M■ i +
ira ra ra' rp ' ry
+M (i -0,5■ i. -0,5■ i );
Y sa > sp > sy ) >
wR = Ln ■ in - 0,5 ■ M ■ i - 0,5 ■ M ■ i +
T rp rp rp > ra > ry
+M ■(i. -0,5■ i -0,5 ■ i );
Y sp > sa > sy ) >
w = L ■ i - 0.5 ■ M ■ i - 0.5 ■ M ■ i. +
T ry ry ry ra rp
+M (i -0.5■ i -0.5■ i.),
Y sy sa sp ) >
(2)
where L is the total phase inductance, H; M is the mutual inductance of the stator and rotor phases, H.
The electromagnetic torque equation of the asynchronous motor is
TEM = 73 ■ [( Z« * r + zsp ' ira + isy ■ ip )"
-(i ■i
sa r
b + k. ■z + z
rp sp ry
Z ■i )!/2.
sy raj J'
Equation of motion of the motor shaft with a single-mass mechanical system
drar / dt = J-(TEM - TC ),
(4)
where Tem is the moment of inertia of the rotating masses on the rotor shaft, Nm; Tc is the static rotational moment on the rotor shaft, Nm.
The mutual inductance is determined using the following formula
M = 2-^/3,
(5)
where L^ is magnetization inductance.
Arranging the nonsymmetrical mode necessitates considering the mutual inductances' modifying. To determine the changes in the mutual inductances of the windings it is necessary to define the degree of the effect of changing in the alternative current impedance of one (or two) windings on the magnetic circuit inductance. In the work (Goolak S., Gerlici J., Tkachenko V., Sapronova S., Lack T., Kravchenko K.
https://doi.org/10.26552/com.C.2019.2.24-31) the established connection is presented between the windings' inductances and their geometrical dimensions. Taking into account the uniformity of the air-gap and expressions for the phase inductances of scattering and phase mutual inductances, it was inferred that the inductances of scattering of each phase and mutual phase inductances can be written in the general form as follows
LY =( l; f.F (aj ),
(6)
where (X is the component, which depends
on the winding geometrical dimensions; (the upper indices X, Y can take 5 or r values and show which windings are considered: stator or rotor. The lower indices i, j can take the values of A, B, C and indicate the windings of which
phases are considered); F(a^ j is the
component, which accounts for the angle shifts between the phase voltages aj and difference between the angle shifts of the phase currents of
the stator and rotor 9y of the corresponding windings in a symmetrical mode.
Since component F(ay, 9y) relates to the symmetrical mode of the motor operation, to consider the connection between the inductances and the winding geometrical parameters it is feasible confining just to component (L'yX , which is equal to
( L'j = /P • Zf • ZY 4 • ^ • (7)
1 p n g
where ^ is the magnetic permeability; n is the number of periods of the current layer spatial distribution, which is relevant to the pairs of poles number p; g = rs - rr is the radial value of the air gap; rs is the stator radius; rr is the rotor radius; zf = wX /1 is the linear density of the
current layer conductor of a corresponding winding; wXj is the number of turns of a corresponding stator winding phase; lXj is the length of a corresponding winding; and lp is the axial length of the air gap.
The inductance of the motor magnetic circuit is defined using the following expression
L»=YZLf, X * Y.
(8)
Equation (8) is obtained in a general form after the substitution of inductance values from (7). This equation is reduced to the form of function, which accounts for the number of the phase winding turns , on which the complex resistance change is designed that simulates the inter-turns short circuits of a various degree.
The modification of the magnetic circuit inductance at a relevant change in the value of the winding complex resistance is estimated using the coefficient that is obtained taking into account (6)—(8) and is expressed in relative units
k=L / L.
(9)
The dependence of the modification of the magnetic circuit inductance coefficient on the value of the change in the phase complex resistance of the stator winding phase (Z) is shown in Fig. 1.
Using the values of the magnetic circuit inductance for the symmetrical mode from Table 1, with account for the coefficient of the winding
complex resistance (9), the value of the magnetic circuit inductance is obtained for the preset conditions of occurrence the nonsymmetrical mode that is induced by the inter-turn short-circuits.
L' = k • L
(10)
The value of the magnetic circuit inductance (obtained using (10) for the nonsymmetrical mode after the substitution into (5) allows us to define the value of the mutual inductance for the preset mode.
1.0
0.9
0.8
0.7
0.6
0.5
k, conx .un.
Z, conv.un.
0.6
0.7
0.8
0.9
1.0
Fig. 1. Dependence of coefficient of magnetic circuit inductance change on the change in complex resistance of stator winding
The parameters' changes obtained were corrected using the simulation model.
During the asymmetric model creation, it is necessary to account for the following factors:
1. The most convenient parameter to determine the inter-turn short-circuit at a certain phase of the motor is the phase resistance.
2. As is seen from (7), the inductance of the phase scattering and mutual inductance are the square function of the number of turns.
3. The active resistance of the winding is defined using the following expression
rs = K • Pe
I • w
mean
q..
(11)
where kr is the coefficient of increasing the active resistance of the winding phase from the thermal action of the enhanced current; pe is the specific resistance of the winding material upon the calculated temperature, Ohm; Imean is the average length of the winding turn, m; w is the number of the winding turns; qe.c is the area of
the cross section of the elementary conductor, m2; ne.c. is the number of the elementary conductors; a the number of the parallel winding paths.
Hence, it follows that the active resistance of the stator phase is proportional to the number of the winding turns. For simplicity of transition
from the full complex resistance to the active resistance, the resistance of the scattering inductance and the mutual inductance depending on the number of turns Table 1 lists the values of these magnitudes, which were used in the research of the asynchronous motor operation with nonsymmetrical stator windings.
Table 2
Values of active, inductive, complex resistance of stator phase, resistance of mutual stator and rotor inductance at different values of complex resistance
Zl/Zlnom zi, om Wi (wi)2 ri, Om xi, Om Xp, Om
1 0.751 1 1 0.5 0.56 0.559
0.9 0.676 0.934 0.872 0.467 0.489 0.547
0.85 0.639 0.9 0.81 0.45 0.454 0.54
0.8 0.601 0.864 0.746 0.432 0.418 0.534
0.72 0.537 0.8 0.64 0.4 0.358 0.522
The established adequacy in values in Table 2 terminate the construction of the simulation model for performing the research of the electromagnetic processes in the asynchronous motor with nonsymmetrical windings..
RESEARCH OF THE EFFECT OF INTER-TURN SHORT-CIRCUITS ON THE TORQUE PULSATION ON THE MOTOR SHAFT AND PHASE CURRENTS' UNBALANCE
Methods for performing the studies of the effect of various forms of inter-turns short-circuits on the motor parameters includes parameters' modeling of the operating stator, simulations of short-circuiting, first only on a single phase A and then a simultaneous short-circuit on two phases of the stator winding:
during the constant short-circuiting of the winding turns of phase A (when the winding resistance is decreased to 80 % versus the nominal value and two cases in addition, when the resistance decrease of phase B winding occurs). For the reduced variants of the winding failures the values of the main parameters are determined in case of the asynchronous motor for the symmetrical mode (of the operating stator), at decreasing complex resistance of phase A by 20 % during permanent complex resistance of phase B, at a decrease in the complex resistance of phase A by 20 % and a simultaneous decrease in the complex resistance of phase B by 10 and 20 %. The results of modeling for various modes of the motor operation are listed in Tables 3 and 4.
Modeling results of asynchronous motor operation in idle-run mode at
failures of the stator windings
Table 3 various kinds of phase
Parameter Failure-free stator Number of unimpared turns of phase A winding - 80%
Number of unimpared turns of phase B winding
100% 90% 80%
Rotor spinning frequency n, rot/min 1498 1498 1498 1498
Average electromagnetic torque Tmidie, H-m 0.3804 0.3822 0.3787 0.3776
Maximum electromagnetic torque Tmax, H-m 0.3804 1.8997 1.6979 1.8895
Minimum electromagnetic torque Tmin, H m 0.3804 -1.134 -0.941 -1.1344
Torque ripple frequency fpuis, Hz 0 100 100 100
Phase A root-mean-square current of stator Iia, A 9.403 11.553 11.99 12.456
Phase B root-mean-square current of stator Iia, B 9.403 9.805 10.923 12.244
Phase C root-mean-square current of stator lie, B 9.403 9.974 10.242 10.513
Electromagnetic torque ripple factor kpuisT, % 0 396.91 348.35 400.41
Unbalance factor of stator phase currents kunbaiii, % 0 18.59 18.59 20.664
In Tables 3, using (12)
4, torque ripple is calculated
Km - Tmn ) / Tmidle )-100%, (12)
where Tmax is the max torque value; Hm; Tmin is the min torque value; H m; Tmin is the is the average torque value.
Table 4
Modeling results of asynchronous motor in nominal mode at different types of phase failures of
stator windings
Parameter Failure-free stator Number of unimpaired turns of phase A winding -80%
Number of unimpaired turns of phase B winding
100% 90% 80%
Rotor spinning frequency n, rot/min 1450 1450 1450 1450
Average electromagnetic torque Tmiddie, H-m 72.443 72.878 73.02 73.24
Maximum electromagnetic torque Tmcix, H-m 72.443 74.938 74.56 75.01
Minimum electromagnetic torque Tmin, H m 72.443 68.886 69.56 69.48
Torque ripple frequency fpuis, Hz 100 100 100 100
Phase A root-mean-square current of stator Iia, A 21.879 25.566 25.52 25.39
Phase B root-mean-square current of stator Iia, B 21.879 20.29 23.34 25.12
Phase C root-mean-square current of stator Iic, B 21.879 20.318 21.9 21.339
Electromagnetic torque ripple factor kpuisT, % 0 4.152 3.424 3.777
Unbalance factor of stator phase currents kunbciii, % 0 24.114 16.53 18.58
The unbalance factor of stator phase currents is determined using the following formula
kM = ((4mx - Ismn ) / Issymmode ) "100%, (13)
where Ismax is the max value of the stator phase current, A; Ismin is the min value of the stator phase current, A; Issym.mode is the value of the phase current at the symmetrical mode, A.
The analysis of the modeling results from Tables 3, 4 show that the torque ripple for the nominal mode of the electric motor operation is substantially lower than that for the idle-run mode. In this context, to perform the estimation of the results obtained, the dependence was created of the change in the electromagnetic torque ripple factor at the decreased value of the complex resistance of the stator phase A by 20 % versus the degree of decrease of phase B complex resistance only for the idle-run mode. During the dependence creation, phase B complex resistance was modified from the nominal value of 100 % (1,0) to 80 % (0,8) with a step of 5 % (0,5) (Fig. 2). According to the results of Tables 3, 4, the graphs were also plotted exhibiting the change in the unbalance factor of the stator phase currents at a constant value of 80 % of phase A complex resistance
versus the nominal induced by the inter-turn short-circuit, depending on the decrease in resistance of the stator phase B winding from 100 % (1.0) (unfaulted) to 80 % (0.8) at a step of 5 % (0.5) for the idle-run mode and nominal (Fig. 3).
420
400
380
360
340.
kPT, %
ZB, p .u.
"1.0 0.95 0.9 0.85 0.8 Fig. 2. Dependence of electromagnetic ripple factor kpT, % on the change in phase A complex resistance by 20 % and simultaneous change in phase B complex resistance of stator in idle-run mode.
It follows from Fig. 2 that the most significant changes occur in the electromagnetic torque pulsation during the change in the complex resistance of the stator phases in the
idle-run mode of the electric motor operation. The unbalance factor of the stator phase current (Fig. 3) during the change both in active and complex resistances of one of the motor phases changes insignificantly.
26
24
22
20
18
16
kimbl,%
kimbl. id
kh nbl.rat(Z) ZB, p.u.
1.0
0.95
0.9
0.85
0.8
Fig. 3. Dependence of unbalance factor of stator phase currents on the change in phase A resistance by 20 % and in idle-run mode simultaneous change in phase B complex resistance of stator in idle-run mode kimbi.idi and nominal mode kimbi.rat
In addition, Fig. 2 shows that changes in the torque pulsation coefficient for the idle-run mode of the motor operation and the unbalance factor of the stator phase currents (see Fig 3) for the nominal mode have a similar parabolic character during the change in the complex resistance of phase B. Unlike the inter-turn short-circuit at a single stator phase, where the linear character dependence is observed, for the inter-turn short-circuit on two phases the initial decrease in the ripple factor is typical at an increase in the failure degree on the second phase followed by an abrupt increase, which is especially characteristic for the idle-run mode (Fig. 2). The dependence like this can be attributed to the fact that during the complex resistance change on the faulted phase B from the nominal value by 510 %, an intermediate 'levelling' occurs of the complex resistances of the phase windings at the expense of increasing the inductive component of the winding resistance. Upon reaching the decrease in the complex resistance of phase B by
Table 5. Modeling results of torque dependence on the motor shaft (T) and of power output (P2)
on rotor spinning frequency ( n)
over 10 % from nominal, the inductive resource of compensation of the phase complex resistance becomes exhausted, which sharply increases the electromagnetic torque pulsations in the idle-run mode and the unbalance factor of the stator phase currents in the nominal mode.
In addition, it follows from Figs. 2, 3 that both of the torque ripple factor and unbalance factor of the stator phase currents depend more on the change in the phase A complex resistance, than on the change in the active resistance.
It is clear from the dependence character obtained that it is not quite correct to use the torque pulsation on the motor shaft and, hence, ether the vibrodiagnosis methods upon establishing the type and degree of the inter-turn short-circuit.
EFFECT STUDY OF INTER-TURN SHORT-CIRCUIT ON MECHANICAL AND
OPERATIONAL CHARACTERISTICS
The researches of the change in the mechanical and operation motor characteristics upon the inter-turn shirt-circuits are carried out for the following cases: the failure-free stator; upon the inter-turn short-circuit at phase A by 20 % with the unfaulted phase B; upon the inter-turn short-circuit at phase A by 20 % with a simultaneous inter-turn short-circuit at the stator phase B, considering that, first, 10 % and then 20 % of the winding turns of this phase were short-circuited.
During the studies performed in the model it is accepted that as a result of the inter-turn short-circuit in the phases of the corresponding windings of 10-20 % of the general number of the phase turns, the complex resistance of the stator winding changes to 90 and 80 % of the nominal (calculated) value.
Modeling of the processes taking place upon the inter-turn short-circuits of the stator winding was performed for the fixed frequencies of the motor rotor spinning using the aforementioned simulation model. The modeling results are listed in Tables 5-8.
n, rot/min T, Hm P2, kW
Failure-free stator Number of phase A unfaulted winding turns -80% Failure-free stator Number of phase A unfaulted winding turns - 80%
Number of phase B unfaulted winding turns Number of phase B unfaulted winding turns
Tab
e 5 continuation
100% 90% 80% 100% 90% 80%
1425.7 100.865 101.823 102.191 102.633 15.059 15.202 15.257 15.323
1440.8 83.132 84.133 84.65 84.206 12.54 12.694 12.772 12.705
1450.0 72.443 72.878 73.023 73.24 11.0 11.066 11.088 11.121
1470.8 42.923 43.137 43.208 43.191 6.611 6.644 6.655 6.655
1485.8 20.573 20.573 20.573 20.607 3.201 3.201 3.201 3.201
1488.3 16.727 16.727 16.727 16.701 2.607 2.607 2.607 2.607
1490.8 12.824 12.824 12.824 12.804 2.002 2.002 2.002 2.002
1493.3 8.793 8.793 8.793 8.806 1.375 1.375 1.375 1.375
1494.8 6.458 6.458 6.458 6.458 1.012 1.012 1.012 1.012
1496.4 3.8596 3.8596 3.8596 3.8596 0.605 0.605 0.605 0.605
1497.9 1.473 1.473 1.473 1.461 0.231 0.231 0.231 0.231
1498 0 0 0 0 0 0 0 0
Table 6
Modeling results of dependency of total power (5) and reactive power (Qi), consumed from circuit from rotor spinning frequency (n j
n, rot/min S, B-A Qi, B-Ap
Failure-free stator Number of phase A unfaulted winding turns - 80% Failure-free stator Number of phase A unfaulted winding turns - 80%
Number of phase B unfaulted winding turns Number of phase B unfaulted winding turns
100% 90% 80% 100% 90% 80%
1425.7 20.268 21.218 21.964 22.651 10.545 11.643 12.412 13.062
1440.8 16.554 17.391 18.006 18.534 8.585 9.49 10.15 10.661
1450.0 14.44 15.128 15.567 15.804 7.513 8.301 8.877 9.067
1470.8 9.803 10.485 11.232 11.676 6.528 7.32 8.183 8.678
1485.8 7.091 7.726 8.845 9.461 6.137 6.782 7.903 8.537
1488.3 6.782 7.355 8.559 9.221 6.123 6.678 7.878 8.555
1490.8 6.527 7.257 8.254 8.896 6.121 6.822 7.803 8.449
1493.3 6.447 7.171 7.938 8.885 6.237 6.929 7.677 8.632
1494.8 6.333 7.138 7.882 8.81 6.204 6.988 7.722 8.653
1496.4 6.282 6.919 7.543 8.359 6.223 6.846 7.422 8.276
1497.9 6.223 6.912 7.306 7.979 6.199 6.883 7.269 7.943
1498 6.206 6.905 7.294 7.747 6.204 6.799 7.287 7.737
7
Modeling results of active power (Pi) consumed from circuit and stator average current (Iimid) on rotor
spinning frequency (n)_
n, rot/min Pi, kw I1mid, A
Failure-free stator Number of phase A unfaulted winding turns - 80% Failure-free stator Number of phase A unfaulted winding turns - 80%
Number of phase B unfaulted winding turns Number of phase B unfaulted winding turns
100% 90% 80% 100% 90% 80%
1425.7 17.309 17.739 18.12 18.506 30.71 32.149 33.278 34.32
1440.8 14.153 14.574 14.873 15.161 25.082 26.351 27.282 28.082
1450.0 12.332 12.647 12.788 12.944 21.879 22.058 23.586 23.946
1470.8 7.313 7.507 7.694 7.811 14.853 15.887 17.018 17.69
1485.8 3.553 3.701 3.971 4.078 10.744 11.706 13.402 14.335
1488.3 2.916 3.082 3.347 3.439 10.275 11.143 12.968 13.971
1490.8 2.265 2.475 2.691 2.784 9.989 10.996 12.356 13.479
1493.3 1.631 1.846 2.016 2.106 9.768 10.865 11.942 13.462
1494.8 1.273 1.456 1.576 1.656 9.596 10.845 11.492 13.349
1496.4 0.861 1.003 1.104 1.17 9.518 10.484 11.428 12.665
1497.9 0.547 0.628 0.736 0.75 9.429 10.473 11.069 12.089
1498 0.156 0.285 0.328 0.384 9.403 10.467 11.052 11.738
Modeling dependences of coefficient of efficiency (n) and power
frequency (n)
Table 8
coefficient (y) on rotor spinning
n, rot/min n , relative units Y, relative units
Failure-free stator Number of phase A unfaulted winding turns - 80% Failure-free stator Number of phase A unfaulted winding turns - 80%
Number of phase B unfaulted winding turns Number of phase B unfaulted winding turns
100% 90% 80% 100% 90% 80%
1425.7 0.87 0.857 0.842 0.828 0.854 0.836 0.825 0.817
1440.8 0.886 0.836 0.852 0.838 0.855 0.838 0.826 0.818
1450.0 0.892 0.875 0.867 0.859 0.854 0.836 0.821 0.819
1470.8 0.904 0.885 0.865 0.852 0.746 0.716 0.685 0.669
1485.8 0.901 0.865 0.806 0.785 0.501 0.479 0.538 0.431
1488.3 0.894 0.846 0.779 0.758 0.43 0.419 0.391 0.373
1490.8 0.884 0.809 0.744 0.719 0.347 0.341 0.326 0.313
1493.3 0.843 0.745 0.682 0.653 0.253 0.227 0.254 0.237
1494.8 0.795 0.695 0.642 0.611 0.201 0.204 0.2 0.188
1496.4 0.703 0.603 0.548 0.517 0.137 0.145 0.139 0.14
1497.9 0.419 0.368 0.314 0.308 0.078 0.081 0.09 0.094
1498 0 0 0 0 0.025 0.041 0.045 0.05
To define the useful power in Table 5, the following expression is used
p =V( s )2 -(a )2
(18)
P = T ■ ro,
(14)
where T is the motor shaft torque, h-m; and © is the rotor spinning frequency of the motor, rad/s.
The rotor spinning frequency of the motor with a number of pole pairs p=2 is determined using the following expression
ro = n /9.55,
(15)
where n is the rotor spinning frequency of the motor.
The nominal reactive power in Table 6 is determined using the following expression
According to the modeling results from Table 5, the mechanical characteristics are plotted as shown in Fig. 4. Using the data of Tables 5, 6, the dependences of total power that is consumed of the circuit using the nominal value of the useful power p* = p / p (Fig. 5).
Tables 5 and 7 were used to create the dependences of the nominal value of the active power consumed of the circuit pp = p / plrat from the nominal value of the useful power p* = p / p (Fig. 6) and dependence of the average nominal value of the stator phase current I* = t /1 from the nominal value of the
1 mid 1mid 1 mid. rat
useful power p2* = p /p2rat (Fig. 7).
O. = -(u ■( i„ - i ) + u „ (i - i ) +
\ sa \ sß sY J sp \ sy sa J
+u (i - i a )) /J 3.
sy \ sa sß M y
(16)
Nominal total power consumed of the circuit in Table 6 is determined using the following expression
S = u • i + u „ • i a + u ■ i . (17)
1 sa sa sfi sfi sy sy V /
The value of nominal active power consumed of the circuit in Table 7 is defined using (18)
1500
1000
500
n, rpm
Z y/y~Zb 0%-90%
Zioo%- '/ji,-Z80°A ',-80% T, N-m
0 100 200 Fig. 4. Motor mechanical characteristics
20
10
S, kVA Z80%-80% Z80%-90%
z Z100 80% Vo P2*,p.u.
0
0.5
1.0
1.5
Fig. 5. Dependence of total power consumed of circuit (S) on relative value of useful power (P2*)
1.5
1.0
0.5
Pl*,p.u. Z80%-90%• Z80%-80%
Z80%
Zioo% P2*, p.u.
0.5
1.0
1.5
Fig. 6. Dependences of relative value of active power (Pi*) consumed of circuit on relative value of useful power (P2*)
In accordance with the results of Tables 5, 8, the dependences of the coefficient of efficiency (Fig. 8) and power factor (Fig. 9) on the nominal value of useful power p* = p / p .
1.5
1.0
0.5
Il mid*, p.u.
Z80%-80% \
Z80%-90% 0%
------- Z100V 0 P2*. p.u.
0 0.5 1.0 1.5
Fig. 7. Dependences of average relative value of stator phase current (Iimid*) on useful power (P2*) value
1.0
0.8 0.6 0.4 0.2
V, P-u.
W\ Z80% KZ80%-80% %-90%
if Zioo%
P2 *, p.u.
0
0.5
1.0
1.5
Fig. 8. Dependence of coefficient of efficiency (n) on relative value of useful power (P2*)
0 0.5 1.0 1.5
Fig. 9. Dependence of power factor (y) on relative value of useful power (P2*)
The analysis of the modeling results with the account for the dependences obtained shows (Figs. 4-9) that with an increase in the level (degree) of the inter-turn short-circuit at the second phase, compared to the inter-turn short-circuit at a single phase:
- the value of the critical torque increases (Fig. 4);
- the total and active powers that are consumed from the circuit (Figs. 5, 6) to create one and the same frequency of the rotor spinning, increase;
- the average value of the current in the faulted stator phase enhances (Fig. 7);
- the coefficient of efficiency (Fig. 8) and the motor power factor (Fig. 9) decrease with the maximum coefficient of efficiency being shifted to the area of the higher loads.
CONCLUSIONS
This work offers the complex approach to the study of the effect of the inter-turn short-circuit of different types on the parameters and characteristics of the asynchronous motors. To solve this problem:
- the mathematical model of the asynchronous motor was selected to allow modeling the operation of the asynchronous motor with nonsymmetrical windings;
- the motor parameters were verified and corrected to obtain the agreement of the modeling results with the motor calculated parameters;
- the effect was studied of the inter-turn short-circuit at a single phase of the stator winding and at two-phase stator simultaneously on the electromagnetic torque ripple factor and the unbalance factor of the stator phase currents. The studies are performed on assumption that resulting from the inter-turn short-circuiting, the winding active resistance and its complex resistances can change. The research results showed that the highest value of the torque ripple factor is exhibited in the idle-run mode during the change in the complex resistance (at a 20 % inter-turn short-circuit in the case of a single phase failure, the torque ripple factor was 264 %). The unbalance factor of the stator phase currents also increased upon the change in the complex resistance, however, having close values for the idle-run mode and for the nominal mode (16.5 % for the idle-run mode and 16.2 % -for the nominal mode);
- for the inter-turn short-circuit of a single phase a linear dependence is determined for increasing the electromagnetic ripple factor and the unbalance factor of the stator phase currents on the value of the change in the complex resistance value of the stator winding (on the failure degree);
- the studies performed aimed at the effect of the inter-turn short-circuit on the mechanic characteristics showed that with an increase in the inter-turn short-circuit up to 20 % , at the second phase for the two-phase failure of the winding, the motor critical moment increases by 2 %, which is also accompanied by the motor starting torque increase;
- the dependence is obtained to establish the connection between the torque pulsation factor and the unbalance factor of the stator phase currents with respect to the change in the phase A and phase B complex resistance at a simultaneous inter-turn short-circuit at two phases of the motor winding;
- in the process of the studies, it was established that at the motor nominal operational mode, the 20 %-increase in the inter-turn short-circuit, at each phase simultaneously at a two-phase winding failure, causes the increase in the
total power, that is consumed from the circuit by 7.1 %, the active - by 4.2 %, and the average stator phase current - by 7.2 %. This decreases the coefficient of efficiency by 4.78 % and in the power factor by 3.2 %.
The results of this work are the issue of the day in terms of selection of the diagnostic method for the inter-turn short-circuit in the stator winding, when creating the efficient diagnostic system used in the asynchronous motors as part of the drives of the transport electric equipment.
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About authors
Губаревич Олег Владимирович, к.т.н., доцент, зав. каф. судовождения и эксплуатации технических систем на водном транспорте Дунайского института водного транспорта Государственного университета инфраструктуры и технологий.
E-mail: [email protected]
Гулак Сергей Александрович, к.т.н., старший преподаватель кафедры тягового подвижного состава Киевского института железнодорожного транспорта Государственного университета инфраструктуры и технологий. E-mail:
Даки Елена Анатольевна,
д.т.н., доцент, директор Дунайского института водного транспорта Государственного университета инфраструктуры и технологий. E-mail:
Тришин Вячеслав Валентинович,
старший преподаватель кафедры судовождения и эксплуатации технических систем на водном транспорте Дунайского института водного транспорта Государственного университета инфраструктуры и технологий. E-mail:
