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Open Physics

formerly Central European Journal of Physics

Editor-in-Chief: Seidel, Sally

Managing Editor: Lesna-Szreter, Paulina


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Volume 15, Issue 1

Issues

Volume 13 (2015)

Modelling axial vibration in windings of power transformers

Pawel Witczak
  • Corresponding author
  • Institute of Mechatronics and Information Systems, Lodz University of Technology, Lodz, Poland
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  • Other articles by this author:
  • De Gruyter OnlineGoogle Scholar
/ Michal Swiatkowski
Published Online: 2017-12-29 | DOI: https://doi.org/10.1515/phys-2017-0103

Abstract

This paper describes the method of homogenization of material properties applied to windings used in power transformers. Exemplary results of natural modes of vibrations obtained by means of finite elements method are also included.

Keywords: power transformer; winding; vibration; finite elements

PACS: 43.40.+s; 46.40.Ff

1 Introduction

The windings in power transformers have a complex and composite structure which is mechanically highly anisotropic and relatively weak, especially in high voltage units where the amount of insulation material is substantial. The presence of insulation, whose rigidity is about two hundred times less than for copper, is most important when deformations in axial direction are considered. The proper estimation of these phenomena is important for the analysis of the winding resistance against operational short-circuit [1] and also for the winding vibration at load [2, 3, 4, 5, 6]. In either case arises the question of introducing an equivalent material for the winding area because the exact representation of complex geometry and material heterogeneity would require unacceptable computational effort. The significance of winding vibration in power transformers is clearly visible for units with powers of 100 MVA or greater for which the load noise dominates that of magnetostriction origin.

2 Winding structure in power transformers

The typical structure of low and high voltage windings in large power transformers consists of a series of coils axially separated by a set of spacers uniformly distributed along the winding circumference and forming the radial cooling ducts filled with oil. The coils are usually wired with continuously transposed cable (CTC).The above system includes a set of repetitive portions with the same geometry, material structure and electromagnetic excitation. Each portion consists of sectors of a single coil accompanied with four quarters of spacers. The outlook of a sector together with a cross-section of CTC is displayed in Figure 1. The distribution of mechanical and electromagnetic stress acting on this elementary section is quite complex and it depends on the section’s position in the winding. The all further analysis will concern the excitations and constraints in the axial direction only.

Outlook of elementary sector of winding and CTC cross-section
Figure 1

Outlook of elementary sector of winding and CTC cross-section

3 Principle of homogenization

The aim of this investigation is to find the equivalent properties of a homogeneous material having the same outer dimensions (d0,α0,h0) as the sector in Figure 1 and simultaneously, reacting in the same way under external excitation. The equation governing this analysis is the virtual work principle S(V)σijnjuidS=V(S)σijϵijdV(1)

where σij, εij are stress and strain and ui is a virtual displacement. The condition of static equilibrium requires the null value of displacement along the part of outer boundary. If the homogenous volume, having a constant cross-section Sh normal to 0z axis, is subjected to the unidirectional load created by axial displacement of the boundary surface uz0 the equation (1) converts into phShuz0=Ezuzz2Shh0(2)

where ph denotes the pressure on the displaced surface. The strain varies linearly in this case and therefore, we obtain Hooke’s law ph=Ezuz0h0(3)

In other words, the homogenization of some volume of interest means that having the same displacement and elastic energy we can approximate the integral equation Fi=Kui(4)

introducing the artificial stiffness K linking the components of force Fi and displacement ui which are mean quantities for the given volume.

4 Numerical model of winding sector

The transformer windings are significantly pre-stressed in the axial direction. It means that CTC filaments in the area directly under spacers may be assumed to be tightly connected by the friction forces, but outside they can move more or less independently. To designate the equivalent Young modulus in the axial direction a numerical model consisting of two CTC filaments, together with four quarters of a spacer, was developed. Its outlook is shown in Figure 2.

Numerical model of CTC section
Figure 2

Numerical model of CTC section

The model is subjected to virtual, axial symmetric displacements uzm (the same as in the homogenous case) and constrained in the circumferential direction. Results of the calculations are presented in Figure 3.

Strain and stress fields inside CTC section (white is null value)
Figure 3

Strain and stress fields inside CTC section (white is null value)

Observing fields shown in Figure 3 we see that the energy of the deformations σzzεzz is stored in the spacers only, besides, in a uniform manner. It is worth noting that shear stresses are almost absent on the outer surface of the model. The choice of the equivalent homogenous material is made assuming the same axial outer displacement and total energy stored as in a real case. The above remarks lead to the following equation resulting from (1) and (2) Esuz0hs2Vs=Ezuz0h02Vh(5)

where Vs and hs are the volume and height of the spacer and Vh and h0 refer to the homogenous material. After simple manipulations we get an expression describing the relation between the values of axial Young modulus Ez of the equivalent homogenous structure and of the spacer’s material Es Ez=Esh0h0hzα0α1α0(6)

Geometric dimensions are presented in Figure 1. Inserting their values for 120 MVA units we have for HV and LV windings produce the following results: EzHV = 1.47 Es and EzLV = 1.58 Es.

Quite often CTC are hardened by their epoxy filler during the drying process of transformer windings. In such a case we cannot assume that CTC filaments directly contact themselves and we must take into account the amount of relatively soft resin in between. A finite elements model showing the sector of an exemplary CTC is presented in Figure 4. The number of filaments inside is even not odd in order to simplify the analytic expressions. Bearing in mind that the radius of transformer coils is much larger than their thickness, the Cartesian system is used but preserving the notation of axes like in cylindrical coordinates.

Numerical model of CTC
Figure 4

Numerical model of CTC

The virtual displacement was applied along the 0r axis for points belonging to external planes normal to that direction. The remaining outer boundary was left free, creating the one-dimensional load case. Distributions of dominating strain and stress components are presented in Figure 5. The strain has a non-zero value in the areas of epoxy filler only, therefore, the elastic energy is just stored there as well. Observing the profile of displacement ur shown in Figure 6 along axis nr presented in Figure 4, we may conclude that each layer of resin contains almost the same amount of elastic energy.

Strain and stress fields inside CTC cross-section (white is null value)
Figure 5

Strain and stress fields inside CTC cross-section (white is null value)

Radial displacement field inside CTC cross-section
Figure 6

Radial displacement field inside CTC cross-section

The outer dimensions of the CTC cross-section are hr, hz and hα (see Figure 4) and the relative volumes of filler along axes nr and nz are gr and gz. Denoting the virtual displacement value by u0 and Young modulus of filler by Ef we may compute the elastic energy stored in the CTC from W=Efu02grhr2VCTCa(7)

where Va CTC denotes the active volume of the filler VCTCa=grhrhα1gzhz(8)

The same amount of energy stored in the homogenized equivalent material under the same virtual displacement in the radial direction is given by W=Eeru02hr2hrhαhz(9)

what immediately results with the value of equivalent material property in the radial direction is Eer=Ef1gzgr(10)

The property of CTC in the axial direction is obtained by the simple exchange of subscripts Eez=Ef1grgz(11)

When the winding has radial cooling ducts we must repeat the analysis of axial deformation described earlier but now with two areas having different elastic properties: Es for spacer and Eez for CTC. Applying the one-dimensional virtual displacement u0 to the outer surfaces of the spacers we must find the unknown displacement u1 on the boundary between spacer and CTC. It results from stress equilibrium σzz=Esu0u1hs=Eezu1hz(12)

where hs is spacer thickness.

Cross-section of two-body winding sector
Figure 7

Cross-section of two-body winding sector

Elastic energy stored now has two components W1 for spacer, W2 for CTC and it is calculated from W1=Esu0u1hs2hrhsα0α1W2=Eezu1hz2hrhzα0α1(13)

The sum of W1 and W2 must be equal to energy in the homogenous material W having larger axial and circumferential size W=Eeqzu0hz+hs2hrhz+hsα0(14)

The equivalent material property in the axial direction of the winding sector containing the CTC turns and spacer is noted here by Eeqz. Equating (12) and (13) and making some simple manipulations we get the final expression Eeqz=11gsEez+gsEsα0α1α0(15)

where gs is the relative size of the spacer gs=hshs+hz(16)

Equation (14) is an extension of (6) for two elastic materials subjected to the same stress. It is necessary to remember that amount of insulation material inside CTC depends heavily on its type and its stiffness has a non-linear shape against the pre-stress value. The remaining moduli of an orthotropic material, namely Eeqr and Eeqα are calculated in an analogous way. It should be underlined that material having orthotropic properties needs to also specify three shear moduli and three Poisson factors. The shear moduli are obtained by similarly applying the virtual displacement but now in tangent direction. The Poisson factors are calculated from their definition as the ratio of strain along two perpendicular axes.

5 Exemplary results

The winding area in a 120 MVA transformer was modelled using solid and shell elements having orthotropic properties, where windings with axial wedges were constructed within cylindrical coordinates but support plates were modelled under theCartesian system. All materials used in the winding zone have a significant anisotropy. For example, the equivalent material in a HV winding has the following properties along cylindrical coordinates: (Er, Eα, Ez) = (3.2, 67.8, 0.54) GPa and the pressboard is represented in Cartesian system by (Ex, Ey, Ez) = (9.1, 6.8, 0.5) GPa.

Finite elements model of of phase windings in 120 MVA transformer (1/8 volume shown)
Figure 8

Finite elements model of of phase windings in 120 MVA transformer (1/8 volume shown)

The natural mode of vibration having the lowest frequency with dominating axial displacements is presented in Figure 9. It was obtained assuming the core and steel supports to be infinitely stiff.

Shape of natural mode of vibration of winding zone, f = 204 Hz (color map shows axial displacement)
Figure 9

Shape of natural mode of vibration of winding zone, f = 204 Hz (color map shows axial displacement)

Besides the axial deformation strongly coupled in space with the axial forces present in winding we also see the elliptic deformation varying along the winding height which in turn corresponds to the circumferential non-uniformity of radial forces.

6 Conclusions

The analysis presented above clearly indicates the necessity of representation of transformer windings for vibration investigations by anisotropic materials. The main difficulty here is to get the proper values of these parameters which depend on pre-stress of the winding zone and also on distribution of insulation inside the CTC area. The careful measurements of particular properties of elements of winding structure connected with a mathematical model of the winding are essential for the accuracy of the final results.

References

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    Minhas M.S.A., Dynamic Behaviour of Transformer Winding under Short-Circuits, PhD thesis, 2007, Johannesburg Univ. Google Scholar

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    Wang Y., Pan J., Jin M., Finite Element Modelling of the Vibration of a Power Transformer, Proceedings of Acoustics, 2011, paper 34, Gold Coast Google Scholar

  • [3]

    Majer K., Analysis of Vibration and Noise in Converter Transformers, Lodz University of Technology, 2013, ZN 1178, (in Polish) Google Scholar

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    Ertl M., Landes H., Investigation of load noise generation of large power transformer by means of coupled 3D FEM analysis, COMPEL, 2007, 26, 3, 788-799. CrossrefWeb of ScienceGoogle Scholar

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    Reyne G., Magnin H., Berliat G., Clerc C., A Supervisor for the Successive 3D Computations of Magnetic, Mechanical and Acoustic Quantities in Power Oil Inductors and Transformers, in Magnetics, IEEE Transactions on, 1994, 30, 5, 3292-3295. Google Scholar

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    Rausch M., Kaltenbacher M., Landes H., Lerch R., Combination of Finite and Boundary Element Methods in Investigation and Prediction of Load-Controlled Noise of Power Transformers, Journal of Sound and Vibration, 2002, 250, 2, 323-338. CrossrefGoogle Scholar

About the article

Received: 2017-11-03

Accepted: 2017-11-12

Published Online: 2017-12-29


Citation Information: Open Physics, Volume 15, Issue 1, Pages 862–866, ISSN (Online) 2391-5471, DOI: https://doi.org/10.1515/phys-2017-0103.

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© 2017 Pawel Witczak and Michal Swiatkowski. This work is licensed under the Creative Commons Attribution-NonCommercial-NoDerivatives 4.0 License. BY-NC-ND 4.0

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