Research Article  Open Access
Chong Zeng, Song Huang, Yongming Yang, Guanghou Zhou, "Influence of End Structure on Electromagnetic Forces on End Winding of a 1550 MW Nuclear Generator", International Journal of Rotating Machinery, vol. 2017, Article ID 9545238, 12 pages, 2017. https://doi.org/10.1155/2017/9545238
Influence of End Structure on Electromagnetic Forces on End Winding of a 1550 MW Nuclear Generator
Abstract
A 3D electromagnetic model of the end region of a 1550 MW nuclear generator is set up. The electromagnetic forces on the involute and nose parts of the end winding under a rated operation are obtained through the 3D timestep finite element method. The electromagnetic forces on different coils in the same phase are analyzed. By changing the rotor’s relative length and stator coil’s linear length in the 3D electromagnetic model, the electromagnetic force distributions on the end winding are obtained. The influence of each structure change on the electromagnetic force in different directions is studied in detail. Conclusions that can be helpful in decreasing the electromagnetic forces on the end winding through optimizing the end region design are presented.
1. Introduction
Vibrations caused by electromagnetic forces can severely damage endwinding insulations [1, 2]. Electromagnetic force increases significantly with the increase of generator capacity, thereby making large generators more vulnerable to vibration. Vibration should be decreased to ensure the security of end winding. Simply enhancing and increasing the support structures can decrease the damage of electromagnetic force but will lead to other problems, such as low utilization of materials and high manufacturing cost [3]. Optimizing the electromagnetic design for the end region can decrease electromagnetic force and vibration without extra cost. Research on the influence of end structure on the electromagnetic force on end winding can be a reference for optimization.
The accurate calculation of electromagnetic field in the end region and electromagnetic force on end winding is the basis of studies on electromagnetic force. Many studies focus on calculation.
In the early years, analytical methods were used to calculate the electromagnetic field in the end region. Methods based on the BiotSavart law are the most popular among them [4–6]. However, the errors in the results obtained through analytical methods are large because the end region’s structure is complex. To improve the accuracy, numerical methods are utilized in the calculation. Recently, 3D finite element (FE) method has become the most popular method. Wang et al. [7] proposed full 3D models and methods for coupled electromagnetic and temperature fields in the end region of a large hydrogenerator. They discussed the effect of mesh size on the result of eddy current loss and obtained several meshing principles. Waldhart et al. [8] analyzed the influence of several common simplifications on the accuracy of the 3D FE method’s results and found that the geometric details on the inner diameter, the accurate modeling of the stator winding, and the correct BHcurve of the eddy current material are essential to the electromagnetic field. Liang et al. [9] built a fine 3D geometrical model and calculated the magnetic field and eddy current loss in the end region. Wang et al. [10–14] calculated the electromagnetic field and the eddy current losses in the end region of a 330 MW turbogenerator. The influence of underexcitation [10], copper shield [11–13], and clamping plate [14] on the electromagnetic field and eddy current losses was calculated and discussed. Using the 3D timestep FE method, Huang et al. calculated the magnetic field and the eddy current loss on the end components of a 1550 MW nuclear generator and analyzed the influences of different structural parameters on the magnetic field and the eddy current loss [15].
Relatively few studies focus on the electromagnetic force on end winding. Simplifying the end coil as straight line inductors, Richard et al. [16, 17] calculated the electromagnetic force on the end winding of a 600 MW turbogenerator using the 3D electromagnetic model of the stator end region. Senske et al. [18], Drubel et al. [19], and Grüning and Kulig [20] calculated the electromagnetic force on end winding based on the BiotSavart law to line circuit segments. Albanese et al. [21] proposed a numerical approach based on an integral formulation to calculate the magnetic field and forces on the end winding of a large generator. Zhao et al. [22] built a 3D electromagnetic model of a 600 MW turbogenerator and calculated the electromagnetic force on the end winding using the 3D timestep FE method. Furthermore, the vibrations of the end winding were calculated and subjected to 3D FE structural analysis. None of the studies above analyzed the influence of the end structure on the electromagnetic force on end winding.
In this paper, a 3D FE model of the end region of a 1550 MW nuclear generator is set up. The electromagnetic force on the end winding at rated operation is obtained by the FE method. The rotor relative length and the stator coil linear length are set to different values in the FE model. The radial, tangential, and axial force density distributions in different parts of the end winding are presented. The influence of the two parameters on the electromagnetic force on end winding is analyzed. Conclusions that can help in decreasing the electromagnetic forces on end winding through optimal design are presented.
2. 3D Finite Element Model for Electromagnetic Forces Calculation
2.1. Physical Model
The end region of a halfspeed nuclear generator is quite complex. The end part of cores and windings is 3D in structure. The end region contains three end components: copper shield, press plate, and press finger. The structure of the end region is shown in Figure 1.
2.2. Mathematical Model for Electromagnetic Forces Calculation
To improve computational efficiency, the following are assumed:(i)The distribution of current in the stator and rotor windings is uniform.(ii)The highorder harmonics of current and displacement current are ignored.(iii)The hysteresis effect is ignored. The core material is isotropic [11].(iv)The cross section of the solution domain of the magnetic field calculation is shown in Figure 2.
The solution domain is shown in Figure 2. , , and are the boundaries of the solution domain. By adopting , method, we can express the mathematical model of the end region as follows [23, 24]:where denotes the magnetic vector potential, is the electric scalar potential, is the electrical conductivity, is the angular frequency, and is the source current density.
The axial flux is very small in . Therefore, the symmetric boundary condition, which means no flux passes across the face, is set on . and are far from the stator and rotor cores, and their magnetic fields are weak. Therefore, and satisfy the first boundary condition .
The stator current cannot be calculated from the above model because the solution domain only contains the end region. Thus, an additional 2D model of the generator is required. The solution domain of the 2D model is shown in Figure 3, where is the inner area and is the outer edge of the solution domain.
The mathematical model can be described as follows:
is determined by the stator current and rotor current. When a generator operates at rated condition, the rotor current is constant and the 3phase stator currents are given as follows:where is the angle between and axis, is the synchronous angular velocity, is time, and is the magnitude of stator phase current.
can be calculated with the following formula:where is the rated power, is the rated voltage, and is the power factor angle at rated condition.
Besides, and the rotor current can be calculated by iteration.
With the magnetic field in the end region, the electromagnetic force density can be calculated aswhere is the electromagnetic force density, is the current in the coil, is the crosssectional area of the coil, and is the magnetic flux density.
2.3. Modeling of the Proposed Generator
A 1550 MW nuclear generator is adopted because the electromagnetic force in a large generator is large. The basic parameters of the generator are shown in Table 1.

JMAG 12.1 is used to build the model and perform the calculation. A 3D FE model of the end region is established per the actual design of the proposed generator. The meshing of the FE model is shown in Figure 4. Using a sliding mesh, the rotation of the rotor is considered. The whole model contains 713386 elements and 129854 nodes.
(a)
(b)
A 2D FE model of the generator is set up with ANSYS Maxwell 16.1. The stator and rotor currents are obtained by iteration at a rated condition. The result is shown in Table 2.

2.4. Validation of the Model
The experiment is performed on an 1150 MW nuclear generator because the 1550 MW nuclear generator is not available for the experiment. The FE model of the 1150 MW generator is built on the same principles, and the structure of the 1150 MW nuclear generator is almost the same as but smaller than that of the 1550 MW generator. Therefore, the relative errors of the two FE models have a similar order. Three probes are set as shown in Figure 5. The comparison of the magnetic flux densities at noload operation between the computational and experimental results is shown in Table 3. Table 3 shows that the calculation method is reasonable and the relative error of the calculated result is within 10%.

3. Electromagnetic Forces on End Winding
We should analyze only the electromagnetic force on one winding phase because the generator and the electromagnetic force on each winding phase are symmetric. The electromagnetic forces on phase A are analyzed in this paper. In the proposed generator, a winding phase has eight coils. The eight coils are numbered as shown in Figure 6. An end coil can be divided into several parts and the definition of these parts is shown in Figure 7.
The magnetic fields on different coils in the same phase are different. Therefore, the electromagnetic forces on different coils are also different, as shown in Figure 8. The forces on the involute parts change significantly. Generally, the forces on the upper involute parts increase with the coil number. Conversely, the forces on the lower involute parts decrease with the coil number. The upper involute part suffers the largest force among all the involute parts. The electromagnetic forces on the nose parts are smaller than the forces on the involute parts, and they change slightly.
4. Parametric Study on Electromagnetic Forces on End Winding
Although the force on the nose part is smaller than that on the involute part, the vibration on the nose part is even larger than that on the involute part because of the weak constraint [22]. The influences of the end structure parameters on the electromagnetic force on the involute part and the force on the nose part are analyzed in this section. To simplify the analysis, only the forces on coil 8 are studied in detail. Only the upper involute part and the nose are analyzed because the constraints of the upper and lower involute parts are almost the same.
4.1. Influence of the Relative Length of Rotor
Rotor relative length () is defined as shown in Figure 9. The lengths of the rotor core and winding change with . When the rotor core is longer than the stator core, is positive. Conversely, when the rotor core is shorter than stator core, is negative. To study the influence of the rotor relative length on electromagnetic force, is set to −75, 0, and 75 mm in the FE model.
The electromagnetic force distribution on the involute part at 0.039 s is shown in Figure 10. Most of the forces reach their maximums at the same time because the current in the coil reaches the maximum at 0.039 s. Figure 10 shows that radial force is the largest and increases with . The tangential and axial forces are smaller than the radial force and decrease with the increase of . For the three components, the changes are more significant at the side close to the linear part (the right side of each involute part in Figure 10). When varies from −75 mm to +75 mm, the maximum of the electromagnetic force density varies from 2.3 × 10^{6} N/m^{3} to 2.6 × 10^{6} N/m^{3}, 1.2 × 10^{6} N/m^{3} to 1.0 × 10^{6} N/m^{3}, and 1.8 × 10^{6} N/m^{3} to 1.4 × 10^{6} N/m^{3} in the radial, tangential, and axial directions, respectively.
(a)
(b)
(c)
Figure 11 shows the maximum electromagnetic forces on the involute part with different . Figure 11 shows that the radial force is relatively larger than the tangential and axial forces. When increases from −75 mm to +75 mm, the radial force increases by 13% while the tangential and axial forces decrease by 9% and 12%, respectively.
The electromagnetic force distribution on the nose part is shown in Figure 12. The magnitude of the force density is used to show the change in force strength because the direction of the force density changes to the opposite direction of the axis on some areas of the nose part. Figure 12 shows that the radial and axial force densities increase with . The radial force change mainly appears at the inner side of the nose part, and the axial force change mainly appears at the inner side of the top section of the nose part. When varies from −75 mm to +75 mm, the maximum of the electromagnetic force density varies from 1.9 × 10^{6} N/m^{3} to 2.0 × 10^{6} N/m^{3}, 1.0 × 10^{6} N/m^{3} to 1.0 × 10^{6} N/m^{3}, and 2.1 × 10^{6} N/m^{3} to 2.2 × 10^{6} N/m^{3} in the radial, tangential, and axial directions, respectively.
(a)
(b)
(c)
The maximum electromagnetic forces on the nose part with different rotor relative lengths are shown in Figure 13. The radial force is smaller than the tangential and axial forces because the direction of the radial force on both sides of the nose part are opposite and almost offset each other. When varies from −75 mm to +75 mm, the radial and axial forces increase by 8% and 23%, respectively, while the tangential force almost stays constant.
For large generators, the radial vibration of end winding is the most serious [22]. A relatively short rotor can be adopted to reduce the radial vibration from the source. Both the electromagnetic force on the involute and nose parts are smaller with a relatively short rotor. The axial force on the nose part (especially on the top of the inner side) also decreases. However, the tangential and axial forces on the involute part (especially on the region close to the linear part of the end coil) increase at the same time.
4.2. Influence of Stator Coil Linear Length
The stator coil linear length () is defined in Figure 14 as the length of the lower linear part beyond the stator core. To study the influence of on electromagnetic force, is set to 221, 271, 321, 371, and 421 mm in the FE model.
The electromagnetic force density distributions on the involute part at 0.039 s with different stator coil linear lengths are shown in Figure 15. Figure 15 shows that the radial force decreases slightly with the increasing , and the maximum of the radial electromagnetic force is reduced to 2.3 × 10^{6} N/m^{3} when is 421 mm from 2.7 × 10^{6} N/m^{3} when is 221 mm. The tangential and axial forces increase significantly with . The maximums of the tangential and axial forces increase to 1.1 × 10^{6} N/m^{3} and 1.8 × 10^{6} N/m^{3}, respectively, when is 421 mm from 0.9 × 10^{6} and 1.3 × 10^{6} N/m^{3}, respectively, when is 221 mm.
(a)
(b)
(c)
Figure 16 shows the maximum electromagnetic forces on the involute part with different . Figure 16 shows that the radial force is relatively larger than the tangential and axial forces. When increases from 221 mm to 421 mm, the radial force decreases by 14% while the tangential and axial forces increase by 17% and 24%, respectively.
The distribution of the electromagnetic force density magnitude on the nose part with different is shown in Figure 17. The influence of the stator coil linear length on electromagnetic force on the nose part is small. Generally, the radial force decreases with the increase of the stator coil’s linear length. Conversely, the tangential force increases with the stator coil’s linear length. The axial force is constant against the changes in stator coil linear length.
(a)
(b)
(c)
Figure 18 shows the maximum electromagnetic forces on the nose part with different . When increases from 221 mm to 421 mm, the radial and axial forces decrease by 9% and 17%, respectively, while the tangential force remains almost constant.
To reduce the radial vibration on end winding, a relatively large stator coil linear length can be adopted. Consequently, the radial force on the involute and nose parts and the axial force on the nose part will decrease. In contrast, the tangential and axial forces on the involute part increase.
5. Conclusions
In this paper, a 3D FE model of the end region of a 1550 MW nuclear generator is set up. The electromagnetic force on the stator end winding at a rated operation is calculated. The electromagnetic forces on different coils in the same phase are presented. By changing the rotor relative length and stator coil linear length in the FE model, the influence of these parameters on electromagnetic force is analyzed in detail. The following conclusions are drawn:(1)The electromagnetic force on the involute part varies in different coils at the same phase and the upper involute part of the last coil in the rotation direction suffers the largest force. The electromagnetic force on the nose part is smaller than that on the involute part and changes slightly in different coils.(2)Decreasing the rotor relative length decreases the radial forces on the involute and nose parts. However, decreasing the rotor relative length increases the tangential and axial forces on the involute parts.(3)The stator coil linear length can be increased to decrease the radial forces on the end winding. The radial force on the involute and nose parts decreases significantly but the tangential and axial forces on the involute parts simultaneously increase.
Conflicts of Interest
The authors declare that they have no conflicts of interest.
Acknowledgments
The work is financially supported by the project supported by the National Natural Science Foundation of China (Grant no. 51477015).
References
 D. Shally, M. Farrell, and K. Sullivan, “Generator end winding vibration monitoring,” in Proceedings of the 43rd International Universities Power Engineering Conference (UPEC '08), pp. 1–5, Padova, Italy, September 2008. View at: Publisher Site  Google Scholar
 S. Wan, C. Zhan, X. Yao, Y. Deng, and G. Zhou, “Investigation on electromagnetic forces and experimental vibration characteristics of stator end windings in generator,” Transactions of the Canadian Society for Mechanical Engineering, vol. 38, no. 3, pp. 331–345, 2014. View at: Google Scholar
 H. Yuda, Q. Jiajun, and Q. Guanghui, “Calculation of electromagnetic force and vibration on end winding of turbo generators,” in Proceedings of the 10th National Academic Conference of Structure Engineering, Nanjing, China, 2001 (Chinese). View at: Google Scholar
 J. F. Calvert, “Forces in turbine generator stator windings,” Transactions of the American Institute of Electrical Engineers, vol. 50, no. 1, pp. 178–194, 1931. View at: Publisher Site  Google Scholar
 D. Harrington, “Forces in machine end windings,” Electrical Engineering, vol. 72, no. 2, pp. 153–153, 1953. View at: Publisher Site  Google Scholar
 M. Ohtaguro, K. Yagiuchi, and H. Yamaguchi, “Mechanical behavior of stator endwindings,” IEEE Transactions on Power Apparatus and Systems, vol. 99, no. 3, pp. 1181–1185, 1980. View at: Publisher Site  Google Scholar
 H. Wang, R. Zong, L. Liu, and S. Yang, “Full 3D eddy current and temperature field analysis of large hydrogenerators in different operating conditions,” in Proceedings of the 17th International Conference on Electrical Machines and Systems (ICEMS '14), pp. 3599–3603, Hangzhou, China, October 2014. View at: Publisher Site  Google Scholar
 F. J. Waldhart, J. P. Bacher, and G. Maier, “Modeling eddy current losses in the clamping plate of large synchronous generators using the finite element method,” in Proceedings of the 21st International Symposium on Power Electronics, Electrical Drives, Automation and Motion (SPEEDAM '12), pp. 1468–1473, Sorrento, Italy, June 2012. View at: Publisher Site  Google Scholar
 Y.P. Liang, H.H. Wang, J.T. Zhang, and J. Liu, “Research of end fields and eddy current losses for aircooling steamturbogenerator,” Journal of Electric Machines and Control, vol. 14, no. 1, pp. 29–34, 2010 (Chinese). View at: Google Scholar
 L. Wang, W. Li, F. Huo, S. Zhang, and C. Guan, “Influence of underexcitation operation on electromagnetic loss in the end metal parts and stator step packets of a turbogenerator,” IEEE Transactions on Energy Conversion, vol. 29, no. 3, pp. 748–757, 2014. View at: Publisher Site  Google Scholar
 H. Feiyang, L. Weili, W. Likun, G. Chunwei, Z. Yihuang, and L. Yong, “Influence of copper screen thickness on threedimensional electromagnetic field and eddy current losses of metal parts in end region of large waterhydrogenhydrogencooled turbogenerator,” IEEE Transactions on Industrial Electronics, vol. 60, no. 7, pp. 2595–2601, 2013. View at: Publisher Site  Google Scholar
 H. Feiyang, H. Jichao, L. Weili et al., “Influence of copper shield structure on 3D electromagnetic field, fluid and temperature fields in end region of large turbogenerator,” IEEE Transactions on Energy Conversion, vol. 28, no. 4, pp. 832–840, 2013. View at: Publisher Site  Google Scholar
 L. Wang, F. Huo, W. Li et al., “Influence of metal screen materials on 3D electromagnetic field and eddy current loss in the end region of turbogenerator,” IEEE Transactions on Magnetics, vol. 49, no. 2, pp. 939–945, 2013. View at: Publisher Site  Google Scholar
 W. Likun, L. Weili, X. Yi, and G. Chunwei, “Influence of clamping plate permeability and metal screen structures on threedimensional magnetic field and eddy current loss in end region of a turbogenerator by numerical analysis,” Journal of Applied Physics, vol. 114, no. 19, Article ID 193904, 2013. View at: Publisher Site  Google Scholar
 S. Huang, C. Zeng, Y. Yang, and G. Zhou, “Influence of the end structure on the leakage magnetic field and eddy current loss in a 1,550 MW nuclear generator,” Proceedings of the Chinese Society of Electrical Engineering, vol. 36, pp. 200–205, 2016. View at: Publisher Site  Google Scholar
 N. Richard, F. Duffeau, A. C. Leger, and N. Szylowicz, “Computation of forces and stresses on generator end windings using a 3d finite element method,” IEEE Transactions on Magnetics, vol. 32, no. 3, pp. 1689–1692, 1996. View at: Publisher Site  Google Scholar
 N. Richard, “Calculation of electromagnetic forces on large generator endwindings under fault conditions using a threedimensional finite element method,” Mathematics and Computers in Simulation, vol. 46, no. 34, pp. 257–263, 1998. View at: Publisher Site  Google Scholar
 K. Senske, S. Kulig, J. Kauhoff, and D. Wünsch, “Vibrational behaviour of the turbogenerator stator end winding in case of electrical failures,” in Proceedings of the Conférence Internationale des Grands Rèseaux Electriques, pp. 1–12, Yokohama, Japan, October 1997. View at: Google Scholar
 O. Drubel, S. Kulig, and K. Senske, “End winding deformations in different turbo generators during 3phase short circuit and full load operation,” Electrical Engineering, vol. 82, no. 3, pp. 145–152, 2000. View at: Publisher Site  Google Scholar
 A. Grüning and S. Kulig, “Electromagnetic forces and mechanical oscillations of the stator end winding of turbogenerators,” in Recent Developments of Electrical Drives, pp. 115–126, Springer, The Netherlands, 2006. View at: Google Scholar
 R. Albanese, F. Calvano, G. Dal Mut et al., “Coupled three dimensional numerical calculation of forces and stresses on the end windings of large turbo generators via integral formulation,” IEEE Transactions on Magnetics, vol. 48, no. 2, pp. 875–878, 2012. View at: Publisher Site  Google Scholar
 Y. Zhao, B. Yan, C. Zeng, S. Huang, C. Chen, and J. Deng, “Dynamic response analysis of large turbogenerator stator end structure under electromagnetic forces,” Transactions of China Electrotechnical Society, vol. 31, no. 5, pp. 199–206, 2016. View at: Google Scholar
 J. Cheaytani, A. Benabou, A. Tounzi, and M. Dessoude, “Stray load losses analysis of cage induction motor using 3D finite element method with external circuit coupling,” in Proceedings of the 17th Biennial IEEE Conference on Electromagnetic Field Computation (CEFC '16), Miami, Fla, USA, November 2016. View at: Publisher Site  Google Scholar
 K. Yamazaki, S. Kuramochi, N. Fukushima, S. Yamada, and S. Tada, “Characteristics analysis of large high speed induction motors using 3D finite element method,” IEEE Transactions on Magnetics, vol. 48, no. 2, pp. 995–998, 2012. View at: Publisher Site  Google Scholar
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Copyright © 2017 Chong Zeng et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.