Patent Grant
11984249
This disclosure relates to a grain-oriented electrical steel sheet used for a wound core of a transformer, to a wound core of a transformer using the same, and a method for producing the wound core.
A grain-oriented electrical steel sheet having a crystal texture, in which the <001> orientation, an axis of easy magnetization of iron, are highly aligned with the rolling direction of the steel sheet, is used, in particular, as a core material of a power transformer. Transformers are broadly classified by their core structure into stacked core transformers and wound core transformers. The stacked core transformers have its core formed by stacking steel sheets sheared into a predetermined shape. The wound core transformers have its core formed by winding a steel sheet. The stacked core transformers, at present, are often used in large transformers. Although there are various features included in the transformer core, smaller iron loss is most desired.
From this point of view, important characteristics of a grain-oriented electrical steel sheet used as a core material include smaller iron loss. Further, in order to reduce cupper loss by reducing an excitation current in a transformer, it is necessary that magnetic flux density be high. The magnetic flux density is evaluated using the magnetic flux density B8 (T) at a magnetizing force of 800 A/m. Generally, the higher the degree of accumulation into the Goss orientation, the higher the B8. Generally, the hysteresis loss of an electrical steel sheet having a high magnetic flux density is small, and such an electrical steel sheet is excellent also in iron loss characteristics. To reduce the iron loss of a steel sheet, higher alignment of the crystal orientations of secondary recrystallized grains in the steel sheet with the Goss orientation and reduction of impurities in the steel composition are used. However, the control of crystal orientations and the reduction of impurities have limitations. Therefore, a technique for reducing iron loss by introducing non-uniformity to the surface of a steel sheet using a physical method to subdivide the widths of magnetic domains, i.e., a magnetic domain refining technique, has been developed. For example, Patent Literature 1 and Patent Literature 2 describe heat resistant-type magnetic domain refining methods in which linear grooves, having a predetermined depth, are formed on the surface of a steel sheet. Patent Literature 1 describes means for forming grooves using a gear-type roll. Patent Literature 2 describes means for forming grooves by pressing a knife edge against a steel sheet subjected to final finishing annealing. These means have an advantage in that their magnetic domain refining effect applied to the steel sheet does not disappear even after heat treatment and that they are applicable to wound cores etc.
To reduce transformer iron loss, it is generally contemplated to reduce the iron loss of the grain-oriented electrical steel sheets used as the core material (the material iron loss). In a transformer core, particularly, a three-phase excitation wound core transformer having three-legged or five-legged grain-oriented electrical steel sheets, it is known that the iron loss in the transformer is larger compared to the material iron loss. A value obtained by dividing the iron loss value of a transformer using electrical steel sheets for the core of the transformer (transformer iron loss) by the iron loss value of the material obtained by the Epstein test is generally referred to as a building factor (BF) or a destruction factor (DF). Specifically, in a three-leg or five-legged three-phase excitation wound core transformer, the BF is generally larger than 1.
It has been pointed out as a general knowledge that one main cause that the value of transformer iron loss of a wound transformer is larger than the value of the material iron loss is concentration of magnetic flux on inner wound cores that is caused by the difference in magnetic path length. As shown in
In the transformer core, since the coils are inserted, a joint portion (lap portion 4) in which steel sheets are lap-jointed exists as shown in
Based on the qualitative understanding of the causes of the increase in the transformer iron loss, the following approaches, for example, have been made to reduce the transformer iron loss.
Patent Literature 3 discloses a technique for effectively reducing transformer iron loss. Specifically, an electrical steel sheet having poorer magnetic properties than an electrical steel sheet on an outer side is arranged on an inner side on which a magnetic path length is shorter and magnetic resistance is smaller, and the electrical steel sheet arranged on the outer side on which the magnetic path length is longer and the magnetic resistance is larger has better magnetic properties than the electrical steel sheet on the inner side. Patent Literature 4 discloses a technique for effectively reducing transformer noise. Specifically, a wound core produced by winding a grain-oriented silicon steel sheet is arranged on an inner side, and a magnetic material with lower magnetostriction than such grain-oriented silicon steel sheet is externally wound around the wound core to form a combined core.
PTL 1: Japanese Examined Patent Application Publication No. 62-53579
PTL 2: Japanese Examined Patent Application Publication No. 3-69968
PTL 3: Japanese Patent No. 5286292
PTL 4: Japanese Unexamined Patent Application Publication No. 3-268311
PTL 5: Japanese Patent No. 5750820
NPL 1: The transactions of the Institute of Electrical Engineers of Japan. D, Vol. 130, No. 9, P1087-1093 (2010)
NPL 2: The papers of technical meeting on magnetics, Institute of Electrical Engineers of Japan, MAG-04-224, P27-31 (2004)
As disclosed in Patent Literature 3 and Patent Literature 4, the transformer characteristics can be efficiently improved by utilizing concentration of magnetic flux on the inner wound core and forming the inner wound core and the outer wound core using different materials. However, as described above, as the excitation magnetic flux density increases, the concentration of the magnetic flux is reduced, so that the effect of improving the transformer characteristics is reduced. Moreover, in these methods, since it is necessary to arrange different materials appropriately, the transformer manufacturability deteriorates significantly.
An object of the disclosure is to provide a grain-oriented electrical steel sheet that exhibits an excellent transformer iron loss reducing effect when used for a wound core of a transformer. Another object of the disclosure is to provide a wound core of a transformer that uses such grain-oriented electrical steel sheet and a method for producing such wound core.
The present inventors examined interlaminar transfer between an outer wound core and inner wound cores, the magnetic resistance of joint portions, and an increase in iron loss of a transformer.
Grain-oriented electrical steel sheets having a magnetic flux density B8 of 1.93 T at a magnetizing force of 800 A/m and a thickness of 0.20 mm, 0.23 mm, or 0.27 mm were used to produce transformer cores having a wound core shape shown in
The transformer iron loss and the BF (=the transformer iron loss/the material iron loss) increase as the lap joint length decreases and the sheet thickness increases. Further, the average iron loss of the interlaminar transfer portions and the average iron loss of the lap joint portions increase as the lap joint length decreases and the sheet thickness increases. It is therefore inferred that the iron loss of the interlaminar transfer portions and the iron loss of the lap joint portions are significant factors that determine the magnitude of the transformer iron loss. Thus, It is therefore important to consider what factor determines the magnitude of the iron loss of the interlaminar transfer portions and the magnitude of the iron loss of the lap joint portions.
It is inferred that, from the viewpoint of transfer of magnetic flux in lap portions, the iron loss of the lap joint portions varies due to the following causes. Non-Patent Literature 1 is a document relating to transfer magnetic flux in core joint laps.
From the viewpoint of the magnetic resistance of the joint portion, the above correlation may be due to the following reasons. The width of the Gap portions is generally larger compared to that of the gaps between steel sheets in the stacking direction (≅the thickness of surface coatings on the electrical steel sheets (about several micrometers)), but this depends on the accuracy of assembly. The magnetic resistance for (C) the magnetic flux crossing the Gaps may be larger compared to the magnetic resistance for (A) the transfer magnetic flux and the magnetic resistance for (B) the interlaminar magnetic flux. Therefore, as the magnetic flux density crossing the Gaps increases, the magnetic resistance of the joint portion may increase. The increase in the magnetic resistance of the joint portion may directly cause the iron loss of the joint portion to increase.
Further, it is inferred that the magnetic resistance of the joint portion is a significant factor in the increase in the iron loss of the interlaminar transfer portions. As the magnetic flux density excited in the joint portion increases, (C) the magnetic flux crossing the Gaps increases because (A) the transfer magnetic flux cannot increase beyond a certain level. Therefore, the magnetic resistance of the joint portion increases. To avoid this, interlaminar magnetic flux transfer between the outer wound core and the inner wound cores increases in order to avoid the concentration of the magnetic flux on the inner wound cores and to transfer magnetic flux on the outer wound core. In a wound core in which (C) the magnetic flux crossing the Gaps is large and which has a smaller lap joint length and a greater sheet thickness, in order to reduce (C) the magnetic flux crossing the Gaps as much as possible, the interlaminar magnetic flux transfer between the outer wound core and the inner wound cores is increased to reduce concentration of the magnetic flux on the inner wound cores, so that the magnetic flux density excited in the joint portion is reduced. It is inferred that an increase in the interlaminar magnetic flux transfer causes an increase in in-plane eddy current loss, causing an increase in the iron loss of the interlaminar transfer portions.
Based on the above experimental facts and inferences, it was found that to reduce the transformer iron loss and the BF in a wound transformer, it is desirable to reduce the magnetic flux density crossing the Gaps. Further, to reduce the magnetic flux density crossing the Gaps, it may be desirable to increase the amount of the magnetic flux which transfer in the lap portions. One method to increase the amount of the magnetic flux which transfers in the lap portions is to change the design of the transformer core such that the lap length is increased to increase the area of the lap portions. Another method is to reduce the sheet thickness to increase the number of lap regions to thereby increase the area of the lap portions per unit volume of the joint portions or to use a material having a large permeability for the magnetic flux transfer in the lap portions. In the disclosure, to produce a transformer having excellent iron loss characteristics irrespective of the design of the transformer core, a search was conducted for a material that allows the permeability for the magnetic flux transfer in the lap portions to increase when the material is formed into the transformer core considering the effect of the sheet thickness.
The relation between the magnetic flux density which transfer in the lap portions of the joint portions and material magnetic properties for various materials was investigated. In the investigation, as in the experiment described above, transformer cores having the design in
(Iron loss deterioration ratio under elliptic magnetization)=((WA−WB)/WB)×100 (1)
Here, WA in formula (1) is the iron loss under 50 Hz elliptic magnetization of 1.7 T in an RD direction (rolling direction) and 0.6 T in a TD direction (a direction orthogonal to the rolling direction), and WB is the iron loss under 50 Hz alternating magnetization of 1.7 T in the RD direction.
As for the grain-oriented electrical steel sheets (materials),
Although the reason for the correlation between the iron loss deterioration ratio under the elliptic magnetization and the magnetic flux transfer at the lap portions is unclear, the present inventors contemplate that the reason is as follows. When magnetic flux transfers steel sheets in an out-of-plane direction, magnetic poles are formed at the interfaces between the steel sheets, and this causes a very large increase in magnetostatic energy. Then the magnetization state is changed such that a demagnetizing field is generated in an out-of-plane direction in order to reduce the magnetostatic energy. Specifically, it is inferred that an increase in the number of lancet domain structures in the steel sheets, generation of a demagnetizing field at crystal grain boundaries, etc. occur. For a magnetic domain refined material, it is inferred that an increase in the number of closure domains induced in strain-introduced portions occur. The change in the magnetization state may cause the magnetic flux density which transfer in the lap portions to decrease. Under elliptic magnetization in an in-plane direction, the magnetization direction is momentarily oriented in a <111> direction, which is a hard magnetization direction. Exciting under large elliptic magnetization such as 1.7 T in the RD direction and 0.6 T in the TD direction, magnetic anisotropy energy becomes very large at the moment when the magnetization direction of main magnetic domains rotates in a steel sheet plane from the easy magnetization direction to the hard magnetization direction, and therefore the magnetization state is changed such that a demagnetizing field is generated so as to reduce the magnetic anisotropy energy. In this case, as in the case of the transfer magnetic flux in an out-of-plane direction, the number of lancet domain structures in the steel sheets increases, and a demagnetizing field is generated at crystal grain boundaries. In a magnetic domain refined material, the number of closure domains induced in strain-introduced portions increases. Therefore, the iron loss under elliptic magnetization increases more significantly compared to the iron loss under alternating magnetization only in the easy magnetization direction. Specifically, it is inferred that the iron loss deterioration ratio under elliptic magnetization is correlated with a change in the magnetic flux density which transfer in the lap portions because of the same change factor, i.e., the generation of the demagnetizing field.
It is contemplated from the above inference that the magnitude of the magnetic flux density which transfer in the lap portions or the magnitude of the iron loss under elliptic magnetization can be estimated by parameterizing factors such as an increase in the number of lancet domain structures in the steel sheets, the generation of a demagnetizing field at the crystal grain boundaries, and, in a heat resistant-type magnetic domain refined material prepared by formation of grooves, an increase in leakage magnetic flux in groove-formed portions. Specifically,
As the average β angle of the secondary recrystallized grains increases, the magnetostatic energy increases in proportion to Sin β, and the amount of the lancet domain structures may increase to reduce the magnetostatic energy.
The demagnetizing field generated at the grain boundaries may increase according to the grain boundary area ratio per unit area of steel sheet surface 4t/R.
The area of the groove-formed portions per unit area of the steel sheets surface is (w/a)×10−3. The leakage magnetic flux may increase depending on the groove depth relative to the sheet thickness d/t.
A parameter obtained by summing the three factors, Sin β+4t/R+(w/a/√2)×(10d/t)×10−3, was used to classify the iron loss deterioration ratios of materials under elliptic magnetization. These materials have thicknesses of 0.18 mm to 0.30 mm and various different material factors. The material factors and the measurement results are summarized in Table 2, and the relation between a parameter [Sin β+4t/R+(w/a/√2)×(10d/t)×10−3] disclosed herein and the iron loss deterioration ratio is summarized in
In a wound core using a material which has a large magnetic flux density B8 at a magnetizing force of 800 A/m, i.e., in which the degree of accumulation into the Goss orientation is high, even when the magnetic properties of the material are satisfactory, the magnetic properties of the transformer itself may rather deteriorate. In particular, in a wound core that uses grain-oriented electrical steel sheets in which the B8 is 1.91 T or more and the degree of accumulation into the Goss orientation is very high, the high permeability causes excessive concentration of the magnetic flux on the inner circumferential side, and this may result in the increase of the BF.
Further, in a material which has a large B8 and in which the degree of accumulation into the Goss orientation is very high, the secondary recrystallized grains tend to be coarse, and the diameter R of the secondary recrystallized grains can be as large as 40 mm or more. In this case, the demagnetizing field generated at the crystal grain boundaries is small, and the iron loss deterioration ratio under elliptic magnetization is large as described above, so that the BF increases.
However, by controlling the disclosed parameter within the range of 0.080 or more, the BF can be reduced even when the B8 is 1.91 T or more and the diameter R of the secondary recrystallized grains is 40 mm or more. Therefore, by controlling the B8 to 1.91 T or more, the diameter R of the secondary recrystallized grains to 40 mm or more, and the disclosed parameter within the range of 0.080 or more, grain-oriented electrical steel sheets in which the magnetic property (iron loss) of the material is very small, which allow the BF to be small, and which can form a transformer with very small iron loss can be provided.
0.074
63
0.063
67
0.077
61
0.071
66
0.079
58
0.077
61
0.077
51
0.075
54
0.076
52
0.071
54
The disclosure has been completed based on the above findings. Specifically, the disclosed embodiments have the following structures.
According to one aspect of the disclosure, a grain-oriented electrical steel sheet that, when used for a wound core of a transformer, is excellent in the effect of reducing transformer iron loss is provided.
Another aspect of the disclosure, by controlling the properties of the grain-oriented electrical steel sheet used for a transformer core, interlaminar transfer between an inner wound core and an outer wound core and the magnetic resistance of lap joint portions are reduced, and the transformer iron loss of a wound core transformer can be reduced irrespective of the design of the transformer core.
Still another aspect of the disclosure, when a wound core of a wound core transformer is formed using, as a material, the grain-oriented electrical steel sheet of the disclosure, the wound core transformer obtained has a small building factor.
The disclosed embodiments are described in detail. As described above, a grain-oriented electrical steel sheet that gives excellent transformer iron loss satisfying the following conditions is used for a wound transformer core.
The sheet thickness t of the grain-oriented electrical steel sheet (material) and an iron loss deterioration ratio obtained by subjecting steel sheets under elliptic magnetization defined by formula (1) below satisfy the following relations:
In formula (1), WA is iron loss under 50 Hz elliptic magnetization of 1.7 T in an RD direction (a rolling direction) and 0.6 T in a TD direction (a direction orthogonal to the rolling direction), and WB is iron loss under 50 Hz alternating magnetization of 1.7 T in the RD direction.
The iron loss in formula (1) above is measured as follows.
To keep the iron loss deterioration ratio under the elliptic magnetization within the above range, it is preferable that a plurality of linear grooves extending in a direction intersecting the rolling direction are formed on the surface of the grain-oriented electrical steel sheet (material) such that the width w of the grooves in the rolling direction, the depth d of the grooves, the diameter R of secondary recrystallized grains in the steel sheet, and the average β angle of the secondary recrystallized grains in the steel sheet satisfy the relation represented by formula (2) below.
[Math 3]
Sin β+4t/R+(w/a/√2)×(10d/t)×10−3≥0.080 (2)
In formula (2),
The material properties in formula (2) above are measured as follows.
β: Average β Angle (°) of Secondary Recrystallized Grains
The β angle is defined as the angle between the <100> axis of secondary recrystallized grains oriented in the rolling direction of the steel sheet and the rolling surface. The secondary recrystallization orientation of the steel sheet is measured by X-ray crystal diffraction. Since the orientations of the secondary recrystallized grains in the steel sheet vary, the measurement is performed at points set at a 10 mm RD pitch and a 10 mm TD pitch, and the data measured over a measurement area of (500 mm×500 mm) or larger is averaged to determine the average β angle.
R: Diameter (mm) of Secondary Recrystallized Grains
A coating on the surface of the steel sheet is removed by any chemical or electrical method, and the diameters of the secondary recrystallized grains are measured. The number of crystal grains with a size of about 1 mm2 or larger present in a measurement area with a size of (500 mm×500 mm) or larger is measured by visual inspection or digital image processing, and the average area for a single secondary recrystallized grain is determined. The average area is used to compute a circle-equivalent diameter to determine the diameter of the secondary recrystallized grains.
a: Spacing (mm) Between a Plurality of Linear Grooves Extending in Direction Intersecting Rolling Direction
The spacing is defined as the spacing between linear grooves in the RD direction. When the spacings between the lines (the spacing between the grooves) are not constant, the examination is performed at five points within a longitudinal length of 500 mm, and their average is used. When the line spacing varies in the width direction of the steel sheet, their average is used.
w: Width (μm) of Grooves in Rolling Direction
The surface of the steel sheet is observed under a microscope to measure the width. Since the width of a groove in the rolling direction is not always constant, observation is performed at five points or more along one linear row within a length of 100 mm in a sample, and their average is used as the groove width of the linear row in the rolling direction. Further, five or more linear rows within a longitudinal length of 500 mm in the sample are observed, and their average is used as the width w.
d: Depth (mm) of Grooves
The cross section of the steel sheet at the grooves is observed under a microscope to measure the depth. Since the depth of a groove is not always constant, observation is performed at five points or more along one linear row within a length of 100 mm in a sample, and their average is used as the groove depth in the linear row. Further, five or more linear rows within a longitudinal length of 500 mm in the sample are observed, and their average is used as the depth d.
A method for producing a grain-oriented electrical steel sheet satisfying the above relations is described. Any method other than the following method may be used provided that formula (2) is satisfied by controlling each parameters, and no particular limitation is imposed on the production method.
The average β angle of the secondary recrystallized grains can be controlled by controlling the primary recrystallization texture or using, for example, a coil set for finishing annealing. For example, when finishing annealing is performed under conditions having the coil set as shown in
The diameter (mm) of the secondary recrystallized grains can be controlled by controlling the amount of Goss grains present in the primary recrystallized grains. For example, by increasing the final reduction ratio in cold rolling or increasing friction during rolling to thereby increase the amount of shear strain introduced before primary recrystallization of grains, the amount of the Goss grains in the primary recrystallized grains can be increased. Further, the amount of the Goss grains present in the primary recrystallized grains can be controlled also by controlling the heating-up rate during primary recrystallization annealing. The Goss grains in the primary recrystallized grains serve as secondary recrystallization nuclei during finishing annealing. Therefore, the larger the amount of the Goss grains, the larger the amount of secondary recrystallized grains, and which results in smaller diameter of the secondary recrystallized grains.
Examples of a method for forming a plurality of grooves extending in a direction intersecting the rolling direction and used to obtain the magnetic domain refining effect include existing techniques such as (i) an etching method including applying a resist ink to portions of a cold-rolled sheet other than portions in which grooves are to be formed, subjecting the resulting sheet to electropolishing to form grooves, and then removing the resist ink, (ii) a magnetic domain refining technique including applying a load of 882 to 2156 MPa (90 to 220 kgf/mm2) to a finishing-annealed steel sheet to form grooves with a depth of 5 μm or more in a base steel and subjecting the resulting steel sheet to heat treatment at a temperature of 750° C. or higher, and (iii) a method in which grooves are formed by irradiation with a high-energy density laser beam before or after primary recrystallization or secondary recrystallization. In the disclosed embodiments, any of these groove formation methods may be applied. A production issue with the method including applying a load is control of the wear of a gear type roll. A production issue with the groove formation method using irradiation with a high-energy density laser beam is removal of molten iron. It is therefore preferable to form grooves by subjecting a cold-rolled sheet to electrolytic etching.
A specific production method is described using the groove formation by electrolytic etching of a cold-rolled sheet as an example. The width of the grooves in the rolling direction can be controlled by controlling the width of portions not coated with the resist ink. By controlling the spreading of the resist ink or controlling a pattern on a resist ink applying roll, linear grooves having a constant width in the width direction of the steel sheet can be formed. The depth of the grooves can be controlled by the conditions for subsequent electrolytic etching. Specifically, the depth of the grooves is controlled by adjusting the electrolytic etching time or current density.
No particular limitation is imposed on the width of the grooves in the rolling direction provided that formula (2) above is satisfied. However, excessively narrower width induces magnetic poles coupling, leading to an insufficient magnetic domain refining effect. Excessively wider width, to the contrary, reduces the magnetic flux density B8 of the steel sheet. Therefore, the width is preferably from 40 μm to 250 μm inclusive. No particular limitation is imposed on the depth of the grooves provided that formula (2) above is satisfied. However, excessively small depth leads to an insufficient magnetic domain refining effect. Excessively larger depth reduces the magnetic flux density B8 of the steel sheet. Therefore, the depth is preferably from 10 μm or more and about ⅕ or less of the sheet thickness inclusive.
As for the spacing of the plurality of grooves extending in the direction intersecting the rolling direction, the spacing between the grooves formed can be controlled during their production process using any of the above methods. Excessively larger spacing between the grooves reduces the magnetic domain refining effect obtained by the grooves. Therefore, the spacing between the grooves is preferably 10 mm or less.
No particular limitation is imposed on the sheet thickness of the grain-oriented electrical steel sheet of the disclosure. From the viewpoint of manufacturability, onset stability of secondary recrystallization, etc. the sheet thickness is preferably 0.15 mm or more and furthermore 0.18 mm or more. From the viewpoint of reducing eddy-current loss etc., the sheet thickness is preferably 0.35 mm or less and further more preferably 0.30 mm or less.
In the method for producing the grain-oriented electrical steel sheet of the disclosure used for a wound core of a transformer, no limitation is imposed on the matters not directly related to the above properties. However, a recommended preferred component composition and some points of the production method of the disclosure other than the points described above are described.
An inhibitor may be used in the disclosed embodiments. Using, for example, an AlN-based inhibitor, appropriate amounts of Al and N may be added. Using a MnS·MnSe-based inhibitor is used, appropriate amounts of Mn and Se and/or S may be added. Obviously, the both inhibitors may be used in combination. Contents of Al, N, S, and Se, in such case, may be Al: 0.01 to 0.065% by mass, N: 0.005 to 0.012% by mass, S: 0.005 to 0.03% by mass, and Se: 0.005 to 0.03% by mass.
The disclosure may be applied also to a grain-oriented electrical steel sheet in which the contents of Al, N, S, and Se are limited, i.e., no inhibitor is used. The amounts of Al, N, S, and Se in such case may be limited to Al: 100 mass ppm or less, N: 50 mass ppm or less, S: 50 mass ppm or less, and Se: 50 mass ppm or less.
Other basic components and optional components are as follows.
C: 0.08% by Mass or Less
The content of C exceeding 0.08% by mass is difficult to reduce to 50 mass ppm or less at which magnetic aging does not occur during the production process. Therefore, the C content may be 0.08% by mass or less. The lower limit is not provided because secondary recrystallization may occur even in a material containing no C.
Si: 2.0 to 8.0% by Mass
Si is an element effective in increasing the electric resistance of steel and reducing iron loss. However, when the content of Si is less than 2.0% by mass, the effect of reducing the iron loss is insufficient. The content of Si exceeding 8.0% by mass significantly deteriorates workability, and reduces the magnetic flux density. Therefore, the Si content is preferably within the range of 2.0 to 8.0% by mass.
Mn: 0.005 to 1.0% by Mass
Mn is an element necessary for improving hot workability. However, the Mn content being less than 0.005% by mass, the effect of Mn added is small. The Mn content exceeding 1.0% by mass reduces the magnetic flux density of a product sheet. Therefore, the Mn content is preferably within the range of 0.005 to 1.0% by mass.
In addition to the above basic components, the following elements may be appropriately added as components improving the magnetic properties.
At least one selected from Ni: 0.03 to 1.50% by mass, Sn: 0.01 to 1.50% by mass, Sb: 0.005 to 1.50% by mass, Cu: 0.03 to 3.0% by mass, P: 0.03 to 0.50% by mass, Mo: 0.005 to 0.10% by mass, and Cr: 0.03 to 1.50% by mass.
The steel having a component composition adjusted to the above appropriate component composition may be subjected to a standard ingot making process or a standard continuous casting process to form a slab, or a thin cast piece having a thickness of 100 mm or less may be produced by direct continuous casting process. The slab is heated using a common method and then hot-rolled. However, the slab may be subjected directly to hot-rolling without heating after casting. The thin cast piece may be hot-rolled or may be subjected to the subsequent process without the hot-rolling. Then the hot-rolled sheet is optionally annealed and then subjected to cold rolling once or subjected to cold rolling twice or more including process annealing to obtain a final sheet thickness. Then the product is subjected to decarburization annealing and finishing annealing. Then an insulating tension coating is applied, and flattening annealing is performed. In the course of the above process, grooves are formed by electrolytic etching after the cold rolling or formed at some point after the cold rolling by applying a load using a gear type roll or by irradiation with a laser beam. In the composition of the steel product, the C content is reduced to 50 ppm or less by the decarburization annealing, and the contents of Al, N, S, and Se are reduced to the level of inevitable impurities by purification in the finishing annealing.
The characteristics of the three-phase three-legged excitation-type wound core transformer have been described in the present specification. However, the disclosed embodiments are also suitable for wound core transformers having other joint portion structures such as three-phase five-legged cores and single-phase excitation-type cores.
Cold-finished grain-oriented electrical steel sheets having a thickness of 0.18 to 0.30 mm were produced at different reduction ratios and different heating-up rates for primary recrystallization annealing. During the process, electrolytic etching was performed after cold rolling under various conditions to form grooves, and grain-oriented electrical steel sheets having material properties shown in Table 3 were obtained. These electrical steel sheets were subjected to two-dimensional magnetic measurement by the method described in the present description to thereby measure their iron loss deterioration ratio under elliptic magnetization. Transformer wound cores A to C having core shapes shown in
0.074
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0.063
67
0.060
68
0.077
63
0.072
67
0.047
75
0.076
57
0.074
62
0.060
62
0.077
52
0.075
54
0.069
54
0.075
52
0.072
55
0.067
53
| Number | Date | Country | Kind |
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| 2018-014244 | Jan 2018 | JP | national |
| Filing Document | Filing Date | Country | Kind |
|---|---|---|---|
| PCT/JP2019/003399 | 1/31/2019 | WO |
| Publishing Document | Publishing Date | Country | Kind |
|---|---|---|---|
| WO2019/151399 | 8/8/2019 | WO | A |
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| 20170263357 | Senda | Sep 2017 | A1 |
| 20200373046 | Inoue | Nov 2020 | A1 |
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