PROPOSAL FOR ADDITION OF IEC 34-4 STANDARD IN PART FOR DETERMINATION OF POTIER REACTANCE
|
|
- Alyson Benson
- 5 years ago
- Views:
Transcription
1 PROPOSAL FOR ADDITION OF IEC 34-4 STANDARD IN PART FOR DETERMINATION OF POTIER REACTANCE M. M. Kostic * Electrical Engeneering Institute Nikola Tesla, Belgrade, SERBIA* Abstract: On the base of ones investigations results author comes to new conclusion: that the Potier reactance values depend almost only from of turbogenerators reactive currents (i aq = i an sinφ), for given voltage values. This new rule is prove by general qualitative analysis, and then it is checking for the region about rated values active and reactive power, on the example of the considering turbogenerator GTHW 360 (360 MW). Potier reactance values (x P ) are determined with sufficiently accuracy by new method which is published recently by this author. It proposes change of corresponding standard IEC 34-4/1985: ROTATION ELECTRICAL MACHINES, Part 4: Methods for determining synchronous machine quantities from tests, in the part for determination of the Potier reactance. It is proposed that it determined by of the excitation current corresponding to the rated voltage and armature current value i = i an sinφ n, at zero-power factor (overexcitation), and for some characteristic values which would be convenient for construction of turbogenerator capable curve (P-Q curve). Key words: turbogenerator, rotor saturation, leakage reactance, Potier reactance, excitation current, reactive load test, capable curve. 1. INTRODUCTION The excitation (field) current required operating the SG at rated steady-state active power, power factor, and voltage is a paramount factor in the thermal design of a machine. To determine the excitation current under specified load conditions, the Potier reactance X p (or leakage reactance X l ), the unsaturated d and q reactance X du and X qu, armature resistance R a, and the open-circuit saturation curve e 0 (i f ) are needed. Methods for determining the Potier reactance is especially important. It takes into account the additional of the field winding on load and in the overexcited region and is greater than real value of the armature leakage reactance (X p > X l ). The accurate determination of the armature leakage reactance of synchronous machines is essential for the analysis of these machines [l-5]. Although numerical techniques for calculating this
2 reactance have been suggested in the literature, there has not been a practical method for determining its accurate value experimentally owing to the fact that it is difficult to measure the armature leakage flux directly [6, 7]. For experimental machines, search coils inserted in the air gaps of the machines have been used to detect this leakage flux [5]. In general, the armature leakage reactance is usually approximated by the Potier reactance measured at rated terminal voltage [8, 9]. However, the values of the Potier reactance of synchronous machines measured at rated terminal voltage could be much larger than those of the armature leakage reactances [1, 10]. By ours investigation [11] it is confirmed that the discrepancies between the values of the Potier reactance and the armature leakage reactance of four synchronous machines could be as high as 50%. Recent investigations on experimental synchronous machines have also resulted in the same observation [l2]. Instead of measuring the Potier reactance at rated terminal voltage, March and Crary proposed [l] that measuring the Potier reactance at a higher value of the terminal voltage could result in a more accurate value of the armature leakage reactance. However, the application of this method is difficult since the machine under test may not be able to stand the high values of the field current at which the armature leakage reactance is well approximated by the Potier reactance. In order to obtain more accurate values of the armature leakage reactance without any risk to the machines under test, an alternative method is proposed [l]. However, that it is more important to establish the Potier reactance real values then the accurate values of the armature leakage reactance, one can to be shown on the base of the following facts: 1. Leakage reactance X l is nearly independent of the saturation of the magnetic circuit and is therefore assumed to be a constant. 2. The saturation curve of the synchronous generator under load conditions is assumed to be the same as the open-circuit characteristics. According to this assumption, the field leakage flux is assumed to have the same effect under load conditions as it has at no-load. Any error introduced by the use of the open-circuit characteristic is empirically compensated for by use of the Potier reactance (X p >X l ). 3. The field MMF equivalent to the armature MMF and component corresponding of field current (I af ) can be found from unsaturated armature reactance (X a ). 4. The air gap is assumed to be uniform so that the direct-axis synchronous reactance X d is equal to the quadrature axis synchronous reactance X q. For nonsalient-pole synchronous machine (turbogenerator), practically X d = X q. The unsaturated direct-axis synchronous reactance is calculated by equation X du = X a + X l. In numerous investigations [1, 6, 10, l5] one is shown that Potier reactance values depends from of the terminal voltage values. In addition to, on the base ours investigations [l2, 13] it is shown that the Potier reactance depends essentially and from reactive load values, for the given voltage value.
3 It have been reason that, in this paper, is proposed change and addition of the Standard IEC 34-4/1985, in part for determination of Potier reactance [9], which is presented in Appendix THE POTIER REACTANCE DEPENDENCE FROM (REACTIVE) LOADS An equivalent reactance used in place of the armature leakage reactance to calculate the excitation on load by means of the Potier methods. It takes into account the additional of the field winding on load and in the overexcited region and is greater than real value of the armature leakage reactance. At rated voltage tests, the Potier reactance X p may be larger than the actual leakage reactance by as much as 20 to 30% [l5]. By ours investigation [l2] it is confirmed that the discrepancies between the values of the Potier reactance and the armature leakage reactance of four synchronous machines could be as high as 50%. About a half mentioned increasing origins from (reactive) load values, for the given voltage value. Namely, the additional leakage flux of the field winding on load, in the overexcited region, leads additionally increasing Potier reactance X p. It have been reason that, in this paper, is proposed change and addition of the Standard IEC 34-4/1985, "ROTATION ELECTRICAL MACHINES, Part 4: Methods for determining synchronous machine quantities from tests" in part for determination of Potier reactance [9]. One is proposed that X p it determines by of the excitation current corresponding to the rated voltage and armature current value i = i an sinφ n, at zero-power factor (overexcitation), and for some characteristic values which would be convenient for construction of turbogenerator capable curve (P-Q curve). Namely, on the base of ones investigations results [13] author comes to new conclusion: that the Potier reactance values depend practically only from of turbogenerator reactive currents (i aq = i an sinφ), for given voltage values. This new rule is proved: a) first, by qualitative analysis, and b) then it is checking on the example of the considering turbogenerator GTHW 360 (360 MW), for the region of active and reactive loads relevant values [12, 13]. Potier reactance values (x p ) are determined with sufficiently accuracy by new method which is published recently by this author [14]. Standard graphical method is used for determination of Potier reactance [9], which is presented in Appendix 1 (Figures A1 and A2), by the following data: a) from the no-load saturation and sustained three-phase short-circuit characteristics, and b) of the excitation current corresponding to the rated voltage and rated armature current at zero power-factor (overexcitation). If, during overexcitation test at zero power-factor, the voltage and current differs from rated value by not more then ± 0.15 per unit, a graphical method is used for the determination of the excitation current corresponding to the rated voltage and current [1]. On the contrary, author this paper
4 proposes that overexcitation test at zero power-factor be performed for three (four) values armature current (I a ) and corresponding generator voltages, i.e.: - I a1 = I a,max > I an sinφ N (i.e. Q G1 = Q Gmax > Q GN ), which is corresponding to excitation rated current (I f = I fn ) and U G1 = U G at Q G1 = Q Gmax > Q GN (approximately: point C 1, Figure 1); - I a2 = I an sinφ N (i.e. Q G2 = Q GN ) and U G2 = U G at Q 2 = Q N (approximately: point C 2, Figure 1); - I a3 = 0.8I an sinφ N (i.e. Q G3 0.8Q N ) and U G3 = U G at Q G3 (approximately: point C 3, Figure 1), and - I a4 = (I a1 + I a2 )/2, i.e. Q G4 = (Q Gmax + Q GN )/2 and U G4 = U G4 at Q G4. For different reduced excitation current values (for rated voltage and armature current), Figure 1: i f (A1) < i f (A2) < i f (A3) different values of Potier reactance are obtaining, Figure 2, i.e.: x P (A1) < x P (A2) < x P (A3) On the base of these characteristic values of Potier reactance one would be constructed the corresponding capability curve (P-Q curve) of the test generator. Figure 1: Determination of the excitation current corresponding to the rated voltage and rated current at zero power-factor i f (A1) < i f (A2) < i f (A3) [9] for three experimental point i (C1) > i (C2 > i (C3)
5 Fig. 2: Potier reactance values, X P (A1) <X P (A2) < X P (A3) for three different field current corresponding to the rated voltage and rated current at zero power-factor, i f (A1) < i f (A2) < i f (A3) 3. ANALYSIS OF THE POTIER REACTANCE DEPENDENCE ON THE GENERATOR LOAD AND THE NEW RULE FOR THE DETERMINING THEREOF Based on the results of own investigations [12, 13, 14], the author came to a conclusion: that the value of the Potier reactance, for the given voltage value, depends almost exclusively on the reactive load values (i aq = i a sinφ). The above new rule shall be proved, firstly by qualitative analysis, and then based on the Potier reactance dependence (x P ) on the specific generator s active and reactive load [12]. The values (x P ) shall be determined with high accuracy by means of the new method [14]. In Fig. 3, in addition to the graphic procedure for determination of the Potier reactance (x Pn ) for the rated generator region (u u n,, i i n i φ φ n ), has also been included a part of the graphic determining the Potier reactance value (x Pn,90 ) for the reactive load region with the rated load (u u n,, i i n i φ 90 0 ). The procedure for determination of the Potier reactance (x Pn,90 ) has been running in due orders marked by numbers 7 and 8, and is identical to the procedure applied in determining the value (x Pn ). The reactance values x Pn and x Pn,90 were set by means of the new method [14], by the procedure illustrated in Fig. 3. The magnetization curve of the machine under load i fl (e l ) is given for the specific turbogenerator and also determined by the new method [14]. The Potier reactance value for the rated region (x pn ) set in such manner, as a rule exceeded the same for the reactive load region with the rated current (x Pn,90 ), i.e. x Pn > x Pn,90 (Fig. 3). The explanation lies in the fact that the electromotive forces behind the Potier reactance (e P ) and the dissipation
6 reactance behind the dissipation reactance (e l ) have a larger value in the reactive load region with rated current (u u n,, i i n i φ 90 0 ), i.e e P90 = 0F > OC = e Pn,90 (Fig. 3), so that in such region the turbogenerator magnetic circuit saturation is larger and the corresponding reactances are therefore smaller. In the case of the concrete turbogenerator [12], the Potier reactance value for the rated region (x Pn ) is as much as by around 20% larger. That the Potier reactance value, for the given voltage value, depends almost exclusively on the reactive current load value (i aq = i an sinφ), is shown in Fig. 4. In Fig. 4 is, apart from the Potier reactance value (x Pn ) for the rated generator s generator region (u u n,, i i n i φ φ n ) (i an ), additionally was included a part of the graphic determining the Potier reactance value (x Pn,90 ) for the reactive load region, i i aq = i an sinφ n, i.e. For the region where: u u n,, i i an sinφ n and φ The procedure for determining the Potier reactance value (x Pn,90 ) is running in due order marked by numbers 7 and 8, and is identical to the procedure applied when determining the value (x Pn ). The described procedure was conducted for the same turbogenerator as in Fig.3. Fig. 3: Vector diagrams of electromotive forces behind the Potier reactance (e P ) and electromotive forces behind the dissipation reactance (e l ), and procedure for determining the Potier reactance - for the rated generator region (u u n,, i i n and φ φ n ), from 1-6; - for the reactive load with rated current region (u u n, i i n and φ 90 0 ), from 7-8. That the Potier reactance value, for the given voltage value, depends almost exclusively on the reactive current load value (i aq = i an sinφ), is shown in Fig. 4. In Fig. 4 is, apart from the Potier reactance value (x Pn ) for the rated generator s generator region (u u n,, i i n and φ φ n ) (i an ), additionally was included a part of the graphic determining the Potier reactance value (x Pn,90 ) for the reactive load region i i aq = i an sinφ n, i.e. For the region where: u u n,, i i an sinφ n and φ 90 0.
7 The procedure for determining the Potier reactance value (x Pn,90 ) is running in due order marked by numbers 7 and 8, and is identical to the procedure applied when determining the value (x Pn ). The described procedure was conducted for the same turbogenerator as in Fig.3. Fig. 4: Vector diagrams of electromotive forces behind the Potier reactance (e P ) and electromotive forces behind the dissipation reactance (e l ), and procedure for determining the Potier reactance - for the rated generator region (u u n,, i i n and φ φ n ), from 1-6; -for the reactive load with rated current region i = i an sinφ n (u u n, i i an sinφ n and φ 90 0 ), from 7-8. The Potier reactance value for the rated region (x Pn ) determined in such a way is, as a rule, approximately equal to the value (x P90), of the reactive load region i = i an sinφ n (u u n, i i an sinφ n i φ 90 0 ), i.e. (Fig. 4): x x, for i 90 = i an sinφ n (1), P, n P,90 Based on the equivalence (1) and illustrations in Fig.4, it is possible to write a general equivalence x, for i 90 = i a sinφ n (2), P x P,90 The explanation lies in the two following facts: (1) The electromotive force behind the Potier reactance (e P ) and the electromotive force behind the dissipation reactance (e l ), have approximately the same values in the a) reactive load region i = i an sinφ n and b) in the nominal generator region, i.e. e l90 e ln =0B and e P90 e Pn =0C (Fig. 4), so that the corresponding main turbogenerator s magnetic fluxes are also equivalent. (2) The corresponding components of the longitudinal magnetic dissipation of the excitation coil (of the rotor) are also equivalent as they, just as the components of the longitudinal magnetic dissipation of the stator coil, depend almost exclusively on the reactive load.
8 From (1) and (2) follows that corresponding longitudinal magnetic on the stator and rotor parts are equivalent. The consequence thereof is that the turbogenertor s magnetic circuit dissipation are approximately equivalent. For that reason the Potier reactance values for the rated region and the reactive load region i = i an sinφ n, i.e. x Pn x P90 (Fig. 4) are also approximately equivalent. The above proofs are sufficient for the conclusion: a) that the Potier reactance values, for the given voltage value, depend almost exclusively on the reactive load component (i aq = i an sinφ), and b) to propose a change of standard [9] in the part referring to the determination of the Potier reactance, i.e. in order that it be determined based on the reactive load test i = i an sinφ n, as well as concerning several additional characteristic values, which would be appropriate for the construction of the capability curve ( P-Q curve) of the turbogenerator. The above rule is tested on the example of the considered turbogenerator GTHW 360 (360 MW), by comparing - the measured values of the generator s excitation current for the regions around the rated region (P G P Gn, and Q G Q Gn ), and - the calculated values thereof based on the Potier reactance values (x P ), determined for Q G Q Gn. 4. EXAMPLE OF PROCEDURE APPLICATION AND TEST FOR RATED GENERATOR REGION As an example, the Potier reactance values were determined by the method [14], based on the data from the reactive load test and given generators magnetization characteristics (no-load), I F0 (U 0 ). The results of the Potier reactance calculation are given in Table 1, for four turbogenerator reactive load values GTHW 360, as follows: 1. For values Q G1 =Q Gmax > Q GN, corresponding to the rated excitation current I f = I fn ; 2. For values Q G2 = Q GN, at voltage U G2 = U G for Q G2 = Q N ; 3. For values Q G3 = (Q Gmax + Q GN )/2, at voltage U G3 = U G for Q G3 ; i 4. For values Q G4 0.8Q N, at voltage U G = U G4 for Q G4. It is emphasized that the reactive load test is done with the generator connected to the rigid power network (i.e. at the power plant), and that the generator voltage changes only due to change of drop of voltage at the block transformer, at change of reactive loads. This enables the Potier reactance change to take place in real regions at the change of reactive loads, as only the change thereof leads to perceptible voltage changes at connections of a generator operating in a rigid grid. The required Potier reactance values were determined by the new method [14], and are given in Table 1. From the results in Table 1, it can be seen that the Potier reactance value is significantly
9 reduced (increased) when the reactive load is increased (reduced). Those changes could be larger (up to 30-40%), when turbogenerators of MW in capacity are concerned, and whose magnetic circuit at the stator and rotor part is not even more saturated. This justifies the proposal to determine the value of this reactance by the reactive load test, for the relevant values thereof. Table 1. The data from reactive load test of the turbogenerator GTHW 360, procedure and results of the Potier reactance (x P ) calculation x s =x d p.u. P MW Q Mvar U G kv U G /U Gn / I F A x P p.u. Region with the maximally permitted reactive power(q G,max ), for Cosφ Region with the rated reactive power (Q Gn ), for Cosφ Region with reactive power Q G =(Q Gn + Q G,max )/2, for Cosφ Region with reactive power Q G =0.80Q Gn, for Cosφ For the purpose of testing this position: that the Potier reactance value (virtually) does not change with the active generator power, if the change if the reactive load value stays constant, two regions were considered where the load thereof deviate little from the rated ones in terms of the active and reactive power. In addition to that, for every such region (Table 2), the generator excitation current values (I F ) are as follows: - the excitation current values obtained by measurement (Table 2, type 1a and 2a); and - the excitation current value calculated (Table 2, type 1b and 2b), for the Potier reactance value determined by reactive load test for the above values thereof. The calculated excitation current values of the generator (I F ) differ, in turn, by +0.79% and-0.39%, which is within the accuracy limits of the measured excitation current (I F ) values. The accuracy is expected to be even higher in the region of larger reactive power values, as the corresponding (permitted) active power is smaller and the regions therefore differ less from the referent reactive load regions for which the Potier reactance values are determined. The results of more complete application of this procedure, for the purpose of determining the dependence of the Potier reactance on the (reactive) load values are given in the paper [16].
10 Table 2: Values of excitation currents, for generator voltages and currents about the rated values. Data from the reactive load test, procedure and results of the Potier reactance (x P ) calculation x s =x d P Q U G U G /U Gn x P I F p.u. MW Mvar kv / p.u. A Region 1: 1a. Measured values / b. Calculated values Region 1: 1a. Measured values / b. Calculated values CONCLUSION Based on the results of own research, the author reached an important conclusion: that the Potier reactance values, for the given voltage value, almost exclusively depend on the reactive load (i aq = i a sinφ) component. The above hypothesis was proved, a) firstly by a general qualitative analysis, and b) was then tested on the example of the considered turbogenerator GTHW 360 (360 MW), for two operating regions with active and reactive power around the rated values. The Potier reactance (x P ) values were determined with sufficient accuracy by means of the new method of the author thereof [12]. APPENDIX 1: METHOD FOR DETERMINATION OF POTIER REACTANCE [9] When the synchronous machine is operated as a generator on full load, given methods to calculate X p from measurements are applicable [9]. An equivalent reactance used in place of the armature leakage reactance to calculate the excitation on load by means of the Potier methods. It takes into account the additional of the field winding on load and in the overexcited region and is greater than real value of the armature leakage reactance. The Potier reactance is determined graphically from the no-load and three-phase short-circuit characteristics and the excitation current corresponding to the rated voltage and rated armature current at zero power-factor. The no-load and three-phase short-circuit characteristics are plotted on a diagram (Figure A1) as well as a point (A), the ordinate of which is the rated voltage (u=1) and
11 abscissa is the excitation current (i fb ) measured at rated armature current (i=1) and zero powerfactor (cos φ=0) at overexcitation. To the left from the point A, parallel to the abscissa, a length AF equal to the excitation current (i fk ) for the rated armature short-circuit current is laid off. A line parallel to the initial lower portion of the no-load characteristic is drawn through the point F up to the intersection with the upper part of the no-load characteristic (point H). The length of perpendicular from point H to point G (intersection with AF line) represents the voltage drop on reactance x p at rated armature current. In per unit values x p =HG. u i e (i ) fg i k (i ) f e 0 (i ) H f K F G A K' F' D i fk i fa B i f Fig. A1: Determination of Potier reactance from no-load, e 0 (i f ), and short-circuit, i k (i f ), characteristics and the point A(i f, u) corresponding to the rated voltage and current at zero power-factor If, during the excitation test at zero power-factor, the voltage differs from rated value by not more than ±0.15 per unit, a graphical method is used for the determination of the excitation current corresponding to the rated voltage and current, using the data of the test and the no-load and short circuit characteristics, fig. 1. An experimental point (point C, Figure 2) is plotted on a diagram with the no-load curve of the test machines. This point corresponds to zero power-factor and the measured values of armature current (i), voltage (u) and excitation current (i f ). Vector OD equal to the excitation current, corresponding to the armature current (i) on the short-circuit curve, is laid of along the abscissa axis. From the point C, a length CF equal to OD is laid off towards the no-load saturation characteristic and parallel to the abscissa axis. A the line FH is drawn parallel to the extended straight line portion of the no-load saturation characteristic intersecting the latter at H. Line HC is extended to a point N such that HN/HC=1/i, where is i the current corresponding to point C. The no-load curve is then transferred to the right and downwards parallel to itself and by distance HN. Point A is found on this curve which corresponds to the rated voltage and armature current at zero power-factor.
12 Fig. A2: Graphical method for the determination of the excitation current corresponding to the rated voltage and rated current at zero power-factor [9] REFERENCES [1] A.M. El-Serafi, J. Wu, A new Method for Determining the Armature Leakage Reactance of Synchronous Machines, IEEE Transactions on Energy Conversion, Vol.6, No 1, March 1991, pp.120/125. [2] A. B. J.Reece, and A. Pramanik, Calculation of the End Region Field of A.C. Machines, Proc. IEE, Vol. 112, 1965, pp [3] Slemon, R G., Analytic Models for Saturated Synchronous Machines, IEEE Transactions on Power Apparatus and Systems, Vol. PAS-90, 1971, pp [4] E.A. Abdel-halim, C.D. Manning, Modelling Saturation of Laminated Salient-Pole Synchronous Machines, Proc. IEE, Vol. 134, Pt. B, pp [5] Joseph O. and Thomas, A., An Improved Model far Saturated Salient Pole Synchronous Motors, IEEE Transactions on Energy Conversion, Vol. EC-4, 1989, pp [6] Liwschitz-Garik, M., Electric Machinery, D. Van Nostrand Company Inc., New York, [7] J. C. Flores, Buckley. G. W. and Mc Phtrson Jr. G., The Effects of Saturation on the Armature Leakage Reactance of Large Synchronous Machines, IEEE Transactions on Power Apparatus and Systems, Vol. PAS-103, 1984, pp [8] R. Bourne, Electrical Rotating Machine Testing, Iliffe Books Ltd, London, [9] Standard IEC 34-4/1985, "ROTATION ELECTRICAL MACHINES, Part 4: Methods for determining synchronous machine quantities from tests". [10] J. Wu, Theoretical and Experimental Investigations of the Cross-Magnetizing Phenomenon in Saturated Synchronous Machines, Master s thesis, University of Saskatchewan, [11] Studija, Zavisnost pobudne struje i gubitaka snage u sinhronim generatorima Termoelektrana Nikola Tesla A i B od nivoa reaktivnih opterećenja, Elektrotehnički institut Nikola Tesla, 2008.godine, str.54 (on Serbian). [12] Studija: Određivanje stvarnih dijagrama aktivnih i reaktivnih snaga (P-Q krivih) generatora blokova B1 i B2 u Termoelektani "Kostolac" B, Institut Nikola Tesla Beograd, 2009, str.59 (on Serbian). [13] M.M.Kostić, "Novo pravilo za određivanje Potjeove reaktanse za relevantna opterećenja turbogeneratora", "Elektroprivreda", No , str. XX-XX (on Serbian). [14] M.M.Kostić, "Nova metode za određivanje Potjeove reaktanse sinhronih turbogeneratora", "Elektroprivreda", No 4, 2009, str (on Serbian). [15] Ion Boldea, Synchronous Generators - The Electric Generator Handbook, pp. 512, 2006 by Taylor &Francis Group, Boca Raton London New York, [16] M.M.Kostic, "Construction generator capable curves by of new method for determining of Potier reactance, International Conference Power Plants 2010, Serbia.
Determining the Generator Potier Reactance for Relevant (Reactive) Loads
ELEKTROTEHNIŠKI VESTNIK 81(3): 131-136, 2014 ORIGINAL SCIENTIFIC AER Determining the Generator otier Reactance for Relevant (Reactive) Loads Miloje Kostić Electrical Engeneering Institute Nikola Tesla,
More informationAbstract The capability (P-Q) curve of generator can be determined only on the base of examinations in the power plant, i.e. on the base of: the no-lo
CONSTRUCTION OF GENERATOR CAPABILITY CURVES USING THE NEW METHOD FOR DETERMINATION OF POTIER REACTANCE M.M. Kostić*, M. Ivanović*, B. Kostić*, S. Ilić** and D. Ćirić** Electrical Engineering Institute
More informationCONSTRUCTION OF GENERATOR CAPABILITY CURVES USING THE NEW METHOD FOR DETERMINATION OF POTIER REACTANCE
CONSTRUCTION OF GENERATOR CAPABILITY CURVES USING THE NEW METHOD FOR DETERMINATION OF POTIER REACTANCE M.M. Kostić *, M. Ivanović *, B. Kostić *, S. Ilić** and D. Ćirić** Electrical Engineering Institute
More informationSynchronous Machines
Synchronous Machines Synchronous generators or alternators are used to convert mechanical power derived from steam, gas, or hydraulic-turbine to ac electric power Synchronous generators are the primary
More informationSynchronous Machines
Synchronous Machines Synchronous Machines n 1 Φ f n 1 Φ f I f I f I f damper (run-up) winding Stator: similar to induction (asynchronous) machine ( 3 phase windings that forms a rotational circular magnetic
More informationEquivalent Circuits with Multiple Damper Windings (e.g. Round rotor Machines)
Equivalent Circuits with Multiple Damper Windings (e.g. Round rotor Machines) d axis: L fd L F - M R fd F L 1d L D - M R 1d D R fd R F e fd e F R 1d R D Subscript Notations: ( ) fd ~ field winding quantities
More informationEE 742 Chapter 3: Power System in the Steady State. Y. Baghzouz
EE 742 Chapter 3: Power System in the Steady State Y. Baghzouz Transmission Line Model Distributed Parameter Model: Terminal Voltage/Current Relations: Characteristic impedance: Propagation constant: π
More informationCPPM Mahine: A Synchronous Permanent Magnet Machine with Field Weakening
CPPM Mahine: A Synchronous Permanent Magnet Machine with Field Weakening Juan A. Tapia, Thomas A. Lipo, Fellow, IEEE Dept. of Electrical and Computer Engineering University of Wisconsin-Madison 45 Engineering
More informationECE 325 Electric Energy System Components 7- Synchronous Machines. Instructor: Kai Sun Fall 2015
ECE 325 Electric Energy System Components 7- Synchronous Machines Instructor: Kai Sun Fall 2015 1 Content (Materials are from Chapters 16-17) Synchronous Generators Synchronous Motors 2 Synchronous Generators
More informationAnalytical and numerical computation of the no-load magnetic field in induction motors
Analytical and numerical computation of the no-load induction motors Dan M. Ionel University of Glasgow, Glasgow, Scotland, UK and Mihai V. Cistelecan Research Institute for Electrical Machines, Bucharest
More informationDynamics of the synchronous machine
ELEC0047 - Power system dynamics, control and stability Dynamics of the synchronous machine Thierry Van Cutsem t.vancutsem@ulg.ac.be www.montefiore.ulg.ac.be/~vct October 2018 1 / 38 Time constants and
More informationModule 3 : Sequence Components and Fault Analysis
Module 3 : Sequence Components and Fault Analysis Lecture 12 : Sequence Modeling of Power Apparatus Objectives In this lecture we will discuss Per unit calculation and its advantages. Modeling aspects
More informationLesson 17: Synchronous Machines
Lesson 17: Synchronous Machines ET 332b Ac Motors, Generators and Power Systems Lesson 17_et332b.pptx 1 Learning Objectives After this presentation you will be able to: Explain how synchronous machines
More informationAN EFFICIENT APPROACH FOR ANALYSIS OF ISOLATED SELF EXCITED INDUCTION GENERATOR
AN EFFICIENT APPROACH FOR ANALYSIS OF ISOLATED SELF EXCITED INDUCTION GENERATOR Deepika 1, Pankaj Mehara Assistant Professor, Dept. of EE, DCRUST, Murthal, India 1 PG Student, Dept. of EE, DCRUST, Murthal,
More informationNonlinear Electrical FEA Simulation of 1MW High Power. Synchronous Generator System
Nonlinear Electrical FEA Simulation of 1MW High Power Synchronous Generator System Jie Chen Jay G Vaidya Electrodynamics Associates, Inc. 409 Eastbridge Drive, Oviedo, FL 32765 Shaohua Lin Thomas Wu ABSTRACT
More informationFrom now, we ignore the superbar - with variables in per unit. ψ ψ. l ad ad ad ψ. ψ ψ ψ
From now, we ignore the superbar - with variables in per unit. ψ 0 L0 i0 ψ L + L L L i d l ad ad ad d ψ F Lad LF MR if = ψ D Lad MR LD id ψ q Ll + Laq L aq i q ψ Q Laq LQ iq 41 Equivalent Circuits for
More informationUse of the finite element method for parameter estimation of the circuit model of a high power synchronous generator
BULLETIN OF THE POLISH ACADEMY OF SCIENCES TECHNICAL SCIENCES, Vol. 63, No. 3, 2015 DOI: 10.1515/bpasts-2015-0067 Use of the finite element method for parameter estimation of the circuit model of a high
More informationCHAPTER 3 ANALYSIS OF THREE PHASE AND SINGLE PHASE SELF-EXCITED INDUCTION GENERATORS
26 CHAPTER 3 ANALYSIS OF THREE PHASE AND SINGLE PHASE SELF-EXCITED INDUCTION GENERATORS 3.1. INTRODUCTION Recently increase in energy demand and limited energy sources in the world caused the researchers
More informationGenerators. What its all about
Generators What its all about How do we make a generator? Synchronous Operation Rotor Magnetic Field Stator Magnetic Field Forces and Magnetic Fields Force Between Fields Motoring Generators & motors are
More informationIntroduction to Synchronous. Machines. Kevin Gaughan
Introduction to Synchronous Machines Kevin Gaughan The Synchronous Machine An AC machine (generator or motor) with a stator winding (usually 3 phase) generating a rotating magnetic field and a rotor carrying
More informationUnderstanding the Inductances
Understanding the Inductances We have identified six different inductances (or reactances) for characterizing machine dynamics. These are: d, q (synchronous), ' d, ' q (transient), '' d,'' q (subtransient)
More informationSTEADY STATE AND TRANSIENT ANALYSIS OF INDUCTION MOTOR DRIVING A PUMP LOAD
Nigerian Journal of Technology, Vol. 22, No. 1, March 2003, Okoro 46 STEADY STATE AND TRANSIENT ANALYSIS OF INDUCTION MOTOR DRIVING A PUMP LOAD O. I. Okoro Department of Electrical Engineering, University
More informationMitigating Subsynchronous resonance torques using dynamic braking resistor S. Helmy and Amged S. El-Wakeel M. Abdel Rahman and M. A. L.
Proceedings of the 14 th International Middle East Power Systems Conference (MEPCON 1), Cairo University, Egypt, December 19-21, 21, Paper ID 192. Mitigating Subsynchronous resonance torques using dynamic
More informationAnalytical Model for Sizing the Magnets of Permanent Magnet Synchronous Machines
Journal of Electrical Engineering 3 (2015) 134-141 doi: 10.17265/2328-2223/2015.03.004 D DAVID PUBLISHING Analytical Model for Sizing Magnets of Permanent Magnet Synchronous Machines George Todorov and
More informationLoss analysis of a 1 MW class HTS synchronous motor
Journal of Physics: Conference Series Loss analysis of a 1 MW class HTS synchronous motor To cite this article: S K Baik et al 2009 J. Phys.: Conf. Ser. 153 012003 View the article online for updates and
More information3 d Calculate the product of the motor constant and the pole flux KΦ in this operating point. 2 e Calculate the torque.
Exam Electrical Machines and Drives (ET4117) 11 November 011 from 14.00 to 17.00. This exam consists of 5 problems on 4 pages. Page 5 can be used to answer problem 4 question b. The number before a question
More informationElectromagnetic Energy Conversion Exam 98-Elec-A6 Spring 2002
Front Page Electromagnetic Energy Conversion Exam 98-Elec-A6 Spring 2002 Notes: Attempt question 1 and FOUR (4) other questions (FVE (5) questions in all). Unless you indicate otherwise, the first five
More informationMODELING AND HIGH-PERFORMANCE CONTROL OF ELECTRIC MACHINES
MODELING AND HIGH-PERFORMANCE CONTROL OF ELECTRIC MACHINES JOHN CHIASSON IEEE PRESS ü t SERIES ON POWER ENGINEERING IEEE Press Series on Power Engineering Mohamed E. El-Hawary, Series Editor The Institute
More informationECEN 667 Power System Stability Lecture 18: Voltage Stability, Load Models
ECEN 667 Power System Stability Lecture 18: Voltage Stability, Load Models Prof. Tom Overbye Dept. of Electrical and Computer Engineering Texas A&M University, overbye@tamu.edu 1 Announcements Read Chapter
More informationChapter 4. Synchronous Generators. Basic Topology
Basic Topology Chapter 4 ynchronous Generators In stator, a three-phase winding similar to the one described in chapter 4. ince the main voltage is induced in this winding, it is also called armature winding.
More informationDesign and Characteristic Analysis of LSM for High Speed Train System using Magnetic Equivalent Circuit
IJR International Journal of Railway Vol. 3, No. 1 / March 2010, pp. 14-18 The Korean Society for Railway Design and Characteristic Analysis of LSM for High Speed Train System using Magnetic Equivalent
More information7. Transient stability
1 7. Transient stability In AC power system, each generator is to keep phase relationship according to the relevant power flow, i.e. for a certain reactance X, the both terminal voltages V1and V2, and
More informationNumerical Deterministic Method of Including Saturation Effect in the Performance Analysis of a Single-Phase Induction Motor
International Journal of Engineering Research and Development e-issn: 2278-067X, p-issn: 2278-800X, www.ijerd.com Volume 11, Issue 06 (June 2015), PP.66-74 Numerical Deterministic Method of Including Saturation
More informationGeneralized Theory of Electrical Machines- A Review
Generalized Theory of Electrical Machines- A Review Dr. Sandip Mehta Department of Electrical and Electronics Engineering, JIET Group of Institutions, Jodhpur Abstract:-This paper provides an overview
More informationEE 451 Power System Stability
EE 451 Power System Stability Power system operates in synchronous mode Power system is subjected to a wide range of disturbances (small and large) - Loads and generation changes - Network changes - Faults
More informationECE 421/521 Electric Energy Systems Power Systems Analysis I 3 Generators, Transformers and the Per-Unit System. Instructor: Kai Sun Fall 2013
ECE 41/51 Electric Energy Systems Power Systems Analysis I 3 Generators, Transformers and the Per-Unit System Instructor: Kai Sun Fall 013 1 Outline Synchronous Generators Power Transformers The Per-Unit
More informationROEVER COLLEGE OF ENGINEERING & TECHNOLOGY ELAMBALUR, PERAMBALUR DEPARTMENT OF ELECTRICAL AND ELECTRONICS ENGINEERING ELECTRICAL MACHINES I
ROEVER COLLEGE OF ENGINEERING & TECHNOLOGY ELAMBALUR, PERAMBALUR-621220 DEPARTMENT OF ELECTRICAL AND ELECTRONICS ENGINEERING ELECTRICAL MACHINES I Unit I Introduction 1. What are the three basic types
More informationA Simple Nonlinear Model of the Switched Reluctance Motor
IEEE TRANSACTIONS ON ENERGY CONVERSION, VOL 15, NO 4, DECEMBER 2000 395 A Simple Nonlinear Model of the Switched Reluctance Motor Vladan Vujičić and Slobodan N Vukosavić Abstract The paper presents a simple
More informationTutorial 1 (EMD) Rotary field winding
Tutorial 1 (EMD) Rotary field winding The unchorded two-layer three-phase winding of a small synchronous fan drive for a computer has the following parameters: number of slots per pole and phase q = 1,
More informationProposal of short armature core double-sided transverse flux type linear synchronous motor
Proposal of short armature core double-sided transverse flux type linear synchronous motor Shin Jung-Seob a, Takafumi Koseki a and Kim Houng-Joong b a The University of Tokyo, Engineering Building #2 12F,7-3-1
More informationSynchronous Machines
Synchronous machine 1. Construction Generator Exciter View of a twopole round rotor generator and exciter. A Stator with laminated iron core C Slots with phase winding B A B Rotor with dc winding B N S
More informationConcept Design and Performance Analysis of HTS Synchronous Motor for Ship Propulsion. Jin Zou, Di Hu, Mark Ainslie
Concept Design and Performance Analysis of HTS Synchronous Motor for Ship Propulsion Jin Zou, Di Hu, Mark Ainslie Bulk Superconductivity Group, Engineering Department, University of Cambridge, CB2 1PZ,
More informationThe synchronous machine (detailed model)
ELEC0029 - Electric Power System Analysis The synchronous machine (detailed model) Thierry Van Cutsem t.vancutsem@ulg.ac.be www.montefiore.ulg.ac.be/~vct February 2018 1 / 6 Objectives The synchronous
More informationYou know for EE 303 that electrical speed for a generator equals the mechanical speed times the number of poles, per eq. (1).
Stability 1 1. Introduction We now begin Chapter 14.1 in your text. Our previous work in this course has focused on analysis of currents during faulted conditions in order to design protective systems
More informationAnalytical and Numerical Calculations of Synchronous Motors for Industrial Drives
014 UKSim-AMSS 8th European Modelling Symposium Analytical and Numerical Calculations of Synchronous Motors for Industrial Drives Iossif Grinbaum ABB Switzerland Ltd., Segelhofstrasse 9P 5405 Baden-Dättwil,
More informationMassachusetts Institute of Technology Department of Electrical Engineering and Computer Science Electric Machines
Massachusetts Institute of Technology Department of Electrical Engineering and Computer Science 6.685 Electric Machines Problem Set 10 Issued November 11, 2013 Due November 20, 2013 Problem 1: Permanent
More informationAn Introduction to Electrical Machines. P. Di Barba, University of Pavia, Italy
An Introduction to Electrical Machines P. Di Barba, University of Pavia, Italy Academic year 0-0 Contents Transformer. An overview of the device. Principle of operation of a single-phase transformer 3.
More informationTutorial Sheet Fig. Q1
Tutorial Sheet - 04 1. The magnetic circuit shown in Fig. Q1 has dimensions A c = A g = 9 cm 2, g = 0.050 cm, l c = 30 cm, and N = 500 turns. Assume the value of the relative permeability,µ r = 70,000
More informationParameter Estimation of Three Phase Squirrel Cage Induction Motor
International Conference On Emerging Trends in Mechanical and Electrical Engineering RESEARCH ARTICLE OPEN ACCESS Parameter Estimation of Three Phase Squirrel Cage Induction Motor Sonakshi Gupta Department
More information1 Unified Power Flow Controller (UPFC)
Power flow control with UPFC Rusejla Sadikovic Internal report 1 Unified Power Flow Controller (UPFC) The UPFC can provide simultaneous control of all basic power system parameters ( transmission voltage,
More informationAnalyzing the Effect of Ambient Temperature and Loads Power Factor on Electric Generator Power Rating
Analyzing the Effect of Ambient Temperature and Loads Power Factor on Electric Generator Power Rating Ahmed Elsebaay, Maged A. Abu Adma, Mahmoud Ramadan Abstract This study presents a technique clarifying
More informationSaliency torque and V -curve of permanent-magnet-excited
No. 6] Proc. Japan Acad., 76, Ser. B (2000) 77 Saliency torque and V -curve of permanent-magnet-excited synchronous motor (Contributed By Sakae YAMAMURA, M. J. A. by Sakae YAMAMURA, M.J.A., June 13, 2000)
More informationIncorporation of Asynchronous Generators as PQ Model in Load Flow Analysis for Power Systems with Wind Generation
Incorporation of Asynchronous Generators as PQ Model in Load Flow Analysis for Power Systems with Wind Generation James Ranjith Kumar. R, Member, IEEE, Amit Jain, Member, IEEE, Power Systems Division,
More informationChapter 6. Induction Motors. Copyright The McGraw-Hill Companies, Inc. Permission required for reproduction or display.
Chapter 6 Induction Motors 1 The Development of Induced Torque in an Induction Motor Figure 6-6 The development of induced torque in an induction motor. (a) The rotating stator field B S induces a voltage
More informationPROPERTIES OF THE CO-ENERGY FUNCTION FOR AC MACHINES WITH NON-LINEAR MAGNETIC CIRCUIT
PERIODICA POLYTECHNICA SER. EL. ENG. VOL. 45, NO. 3 4, PP. 223 233 (2001) PROPERTIES OF THE CO-ENERGY FUNCTION FOR AC MACHINES WITH NON-LINEAR MAGNETIC CIRCUIT Tadeusz J. SOBCZYK Institute on Electromechanical
More informationModeling Free Acceleration of a Salient Synchronous Machine Using Two-Axis Theory
1 Modeling ree Acceleration of a Salient Synchronous Machine Using Two-Axis Theory Abdullah H. Akca and Lingling an, Senior Member, IEEE Abstract This paper investigates a nonlinear simulation model of
More informationCHAPTER 2 DYNAMIC STABILITY MODEL OF THE POWER SYSTEM
20 CHAPTER 2 DYNAMIC STABILITY MODEL OF THE POWER SYSTEM 2. GENERAL Dynamic stability of a power system is concerned with the dynamic behavior of the system under small perturbations around an operating
More informationJRE SCHOOL OF Engineering
JRE SCHOOL OF Engineering Class Test-1 Examinations September 2014 Subject Name Electromechanical Energy Conversion-II Subject Code EEE -501 Roll No. of Student Max Marks 30 Marks Max Duration 1 hour Date
More informationIntroduction. Energy is needed in different forms: Light bulbs and heaters need electrical energy Fans and rolling miles need mechanical energy
Introduction Energy is needed in different forms: Light bulbs and heaters need electrical energy Fans and rolling miles need mechanical energy What does AC and DC stand for? Electrical machines Motors
More informationComparative Study of Synchronous Machine, Model 1.0 and Model 1.1 in Transient Stability Studies with and without PSS
Comparative Study of Synchronous Machine, Model 1.0 and Model 1.1 in Transient Stability Studies with and without PSS Abhijit N Morab, Abhishek P Jinde, Jayakrishna Narra, Omkar Kokane Guide: Kiran R Patil
More informationA Power System Dynamic Simulation Program Using MATLAB/ Simulink
A Power System Dynamic Simulation Program Using MATLAB/ Simulink Linash P. Kunjumuhammed Post doctoral fellow, Department of Electrical and Electronic Engineering, Imperial College London, United Kingdom
More informationOutcome of this lecture
Outcome of this lecture At the en of this lecture you will be able to: List the ifferent parts of a synchronous machine Explain the operation principles of the machine Use the equivalent circuit moel of
More informationELECTRICALMACHINES-I QUESTUION BANK
ELECTRICALMACHINES-I QUESTUION BANK UNIT-I INTRODUCTION OF MAGNETIC MATERIAL PART A 1. What are the three basic rotating Electric machines? 2. Name the three materials used in machine manufacture. 3. What
More informationEstimation of the Armature Leakage Reactance using the Constant Excitation Test
Estimation of the Armature Leakage Reactance using the Constant Excitation Test B.T. Araujo, M.S. Han, B. Kawkabani, and E.C. Bortoni Φ Abstract -- The adoption of the best available estimate for the stator
More informationHow an Induction Motor Works by Equations (and Physics)
How an Induction Motor Works by Equations (and Physics) The magnetic field in the air gap from the voltage applied to the stator: The stator has three sets of windings that are aligned at 10 degrees to
More informationMutual Inductance. The field lines flow from a + charge to a - change
Capacitors Mutual Inductance Since electrical charges do exist, electric field lines have a starting point and an ending point. For example, if you have a + and a - change, the field lines would look something
More informationMATLAB SIMULINK Based DQ Modeling and Dynamic Characteristics of Three Phase Self Excited Induction Generator
628 Progress In Electromagnetics Research Symposium 2006, Cambridge, USA, March 26-29 MATLAB SIMULINK Based DQ Modeling and Dynamic Characteristics of Three Phase Self Excited Induction Generator A. Kishore,
More informationPrince Sattam bin Abdulaziz University College of Engineering. Electrical Engineering Department EE 3360 Electrical Machines (II)
Chapter # 4 Three-Phase Induction Machines 1- Introduction (General Principles) Generally, conversion of electrical power into mechanical power takes place in the rotating part of an electric motor. In
More informationSYNCHRONOUS GENERATOR s ROTOR INVESTIGATION OF A HYBRID POWER SYSTEM INCLUDING A.G.
Proc. of the 5th WSEAS/IASME Int. Conf. on Electric Power Systems, High Voltages, Electric Machines, Tenerife, Spain, December 16-18, 25 (pp59-514) SYNCHRONOUS GENERATOR s ROTOR INVESTIGATION OF A HYBRID
More informationThe Operation of a Generator on Infinite Busbars
The Operation of a Generator on Infinite Busbars In order to simplify the ideas as much as possible the resistance of the generator will be neglected; in practice this assumption is usually reasonable.
More informationUNIT I INTRODUCTION Part A- Two marks questions
ROEVER COLLEGE OF ENGINEERING & TECHNOLOGY ELAMBALUR, PERAMBALUR-621220 DEPARTMENT OF ELECTRICAL AND ELECTRONICS ENGINEERING DESIGN OF ELECTRICAL MACHINES UNIT I INTRODUCTION 1. Define specific magnetic
More informationECE 585 Power System Stability
Homework 1, Due on January 29 ECE 585 Power System Stability Consider the power system below. The network frequency is 60 Hz. At the pre-fault steady state (a) the power generated by the machine is 400
More informationNEPTUNE -code: KAUVG11ONC Prerequisites:... Knowledge description:
Subject name: Electrical Machines Credits: 9 Requirement : Course director: Dr. Vajda István Position: Assessment and verification procedures: NEPTUNE -code: KAUVG11ONC Prerequisites:... Number of hours:
More informationProceedings of the 6th WSEAS/IASME Int. Conf. on Electric Power Systems, High Voltages, Electric Machines, Tenerife, Spain, December 16-18,
Proceedings of the 6th WSEAS/IASME Int. Conf. on Electric Power Systems, High Voltages, Electric Machines, Tenerife, Spain, December 16-18, 2006 196 A Method for the Modeling and Analysis of Permanent
More informationCharacteristics Analysis of Claw-Pole Alternator for Automobiles by Nonlinear Magnetic Field Decomposition for Armature Reaction
IEEJ Journal of Industry Applications Vol.6 No.6 pp.362 369 DOI: 10.1541/ieejjia.6.362 Paper Characteristics Analysis of Claw-Pole Alternator for Automobiles by Nonlinear Magnetic Field Decomposition for
More informationDetermination of a Synchronous Generator Characteristics via Finite Element Analysis
SERBIAN JOURNAL OF ELECTRICAL ENGINEERING Vol. 2, No. 2, November 25, 157-162 Determination of a Synchronous Generator Characteristics via Finite Element Analysis Zlatko Kolondzovski 1, Lidija Petkovska
More informationDynamic Behavior of Three phase Inductions Motors as Loads in an Electric Power System with Distributed Generation, a Case of Study.
Dynamic Behavior of Three phase Inductions Motors as Loads in an Electric Power System with Distributed Generation, a Case of Study. Marcelo Rodrigo García Saquicela, Ernesto Ruppert Filho, José Luis Azcue
More informationElectrical Machines and Energy Systems: Operating Principles (Part 2) SYED A Rizvi
Electrical Machines and Energy Systems: Operating Principles (Part 2) SYED A Rizvi AC Machines Operating Principles: Synchronous Motor In synchronous motors, the stator of the motor has a rotating magnetic
More informationECE 422/522 Power System Operations & Planning/ Power Systems Analysis II 2 Synchronous Machine Modeling
ECE 422/522 Power System Operations & Planning/ Power Systems Analysis II 2 Synchronous achine odeling Spring 214 Instructor: Kai Sun 1 Outline Synchronous achine odeling Per Unit Representation Simplified
More informationSymmetrical Components Fall 2007
0.1 Variables STEADYSTATE ANALYSIS OF SALIENT-POLESYNCHRONOUS GENERATORS This paper is intended to provide a procedure for calculating the internal voltage of a salientpole synchronous generator given
More informationM. Popnikolova Radevska, Member, IEEE, M. Cundev, L. Pelkovska
MK0500056 Electromagnetic Characteristics and Static Torque of a Solid Salient Poles Synchronous Motor Computed by 3D-Finite Element Method Magnetics (September 2000) M. Popnikolova Radevska, Member, IEEE,
More informationSynchronous Machines - Structure
Synchronou Machine - Structure Synchronou Machine - Structure rotate at contant peed. primary energy converion device of the word electric power ytem. both generator and motor operation can draw either
More informationA1-203 DAN ZLATANOVICI *, POMPILIU BUDULAN, RODICA ZLATANOVICI. ICEMENERG (Romania)
21, rue d'artois, F-75008 Paris http://www.cigre.org A1-203 Session 2004 CIGRÉ DETERMINATION OF THE ACTUAL PQ DIAGRAM OF THE HYDROGENERATORS, BEING IN SERVICE, IN ORDER TO ESTABLISH THEIR MAXIMUM OPERATING
More informationEddy Current Heating in Large Salient Pole Generators
Eddy Current Heating in Large Salient Pole Generators C.P.Riley and A.M. Michaelides Vector Fields Ltd., 24 Bankside, Kidlington, Oxford OX5 1JE, UK phone: (+44) 1865 370151, fax: (+44) 1865 370277 e-mail:
More informationTURBO-GENERATOR MODEL WITH MAGNETIC SATURATION
TURBO-GENERATOR MODEL WITH MAGNETIC SATURATION R. HADIK Department for Electrotechnics, Technical University, H-1521 Budapest Received May 8, 1984 Presented by Prof. Or. I. Nagy Summary In this paper a
More informationCalculation Improvement of No-load Stray Losses in Induction Motors with Experimental Validation
SERBIAN JOURNAL OF ELECTRICAL ENGINEERING Vol. 12, No. 3, October 2015, 303 320 UDC: 621.313.333-253]:621.372.63 DOI: 10.2298/SJEE1503303K Calculation Improvement of No-load Stray Losses in Induction Motors
More informationThe initial magnetization curve shows the magnetic flux density that would result when an increasing magnetic field is applied to an initially
MAGNETIC CIRCUITS The study of magnetic circuits is important in the study of energy systems since the operation of key components such as transformers and rotating machines (DC machines, induction machines,
More informationPHASOR DIAGRAM OF TRANSFORMER. Prepared By ELECTRICALBABA.COM
PHASOR DIAGRAM OF TRANSFORMER Prepared By ELECTRICALBABA.COM IMPORTANT POINTS FOR PHASOR OF TRANSFORMER Transformer when excited at no load, only takes excitation current which leads the working Flux by
More informationDevelopment of axial flux HTS induction motors
Available online at www.sciencedirect.com Procedia Engineering 35 (01 ) 4 13 International Meeting of Electrical Engineering Research ENIINVIE-01 Development of axial flux HTS induction motors A. González-Parada
More informationRevision Guide for Chapter 15
Revision Guide for Chapter 15 Contents tudent s Checklist Revision otes Transformer... 4 Electromagnetic induction... 4 Generator... 5 Electric motor... 6 Magnetic field... 8 Magnetic flux... 9 Force on
More informationCHAPTER 6 STEADY-STATE ANALYSIS OF SINGLE-PHASE SELF-EXCITED INDUCTION GENERATORS
79 CHAPTER 6 STEADY-STATE ANALYSIS OF SINGLE-PHASE SELF-EXCITED INDUCTION GENERATORS 6.. INTRODUCTION The steady-state analysis of six-phase and three-phase self-excited induction generators has been presented
More informationDC motors. 1. Parallel (shunt) excited DC motor
DC motors 1. Parallel (shunt) excited DC motor A shunt excited DC motor s terminal voltage is 500 V. The armature resistance is 0,5 Ω, field resistance is 250 Ω. On a certain load it takes 20 A current
More informationDefinition Application of electrical machines Electromagnetism: review Analogies between electric and magnetic circuits Faraday s Law Electromagnetic
Definition Application of electrical machines Electromagnetism: review Analogies between electric and magnetic circuits Faraday s Law Electromagnetic Force Motor action Generator action Types and parts
More informationMathematical Modeling and Dynamic Simulation of a Class of Drive Systems with Permanent Magnet Synchronous Motors
Applied and Computational Mechanics 3 (2009) 331 338 Mathematical Modeling and Dynamic Simulation of a Class of Drive Systems with Permanent Magnet Synchronous Motors M. Mikhov a, a Faculty of Automatics,
More informationSYLLABUS(EE-205-F) SECTION-B
SYLLABUS(EE-205-F) SECTION-A MAGNETIC CIRCUITS AND INDUCTION: Magnetic Circuits, Magnetic Materials and their properties, static and dynamic emfs and dforce on current carrying conductor, AC operation
More informationApparatus Models: Transformers
Apparatus Models: Transformers Normally model as series impedance from winding resistance and leakage reactance Positive and negative impedances equal In a Y- transformer that phase shift is in the opposite
More informationUniversity of Jordan Faculty of Engineering & Technology Electric Power Engineering Department
University of Jordan Faculty of Engineering & Technology Electric Power Engineering Department EE471: Electrical Machines-II Tutorial # 2: 3-ph Induction Motor/Generator Question #1 A 100 hp, 60-Hz, three-phase
More informationEEE3405 ELECTRICAL ENGINEERING PRINCIPLES 2 - TEST
ATTEMPT ALL QUESTIONS (EACH QUESTION 20 Marks, FULL MAKS = 60) Given v 1 = 100 sin(100πt+π/6) (i) Find the MS, period and the frequency of v 1 (ii) If v 2 =75sin(100πt-π/10) find V 1, V 2, 2V 1 -V 2 (phasor)
More informationCHAPTER 8 DC MACHINERY FUNDAMENTALS
CHAPTER 8 DC MACHINERY FUNDAMENTALS Summary: 1. A Simple Rotating Loop between Curved Pole Faces - The Voltage Induced in a Rotating Loop - Getting DC voltage out of the Rotating Loop - The Induced Torque
More informationCHAPTER 3 INFLUENCE OF STATOR SLOT-SHAPE ON THE ENERGY CONSERVATION ASSOCIATED WITH THE SUBMERSIBLE INDUCTION MOTORS
38 CHAPTER 3 INFLUENCE OF STATOR SLOT-SHAPE ON THE ENERGY CONSERVATION ASSOCIATED WITH THE SUBMERSIBLE INDUCTION MOTORS 3.1 INTRODUCTION The electric submersible-pump unit consists of a pump, powered by
More information