Patent Application
20250232906
The present invention relates to a three-phase three-legged wound core and a method for producing the same, more particularly, to a three-phase three-legged wound transformer core produced from a grain-oriented electrical steel sheet as a material and to a method for producing the same.
Grain-oriented electrical steel sheets with a crystal structure in which <001> orientation, an axis of easy magnetization of iron, is highly aligned in the rolling direction of the steel sheet are used particularly as iron core materials for power transformers. Depending on the iron core structures, transformers are broadly divided into stacked core transformers and wound core transformers. In a stacked core transformer, steel sheets cut to a predetermined shape are stacked to form an iron core. On the other hand, an iron core in a wound core transformer is formed by winding a steel sheet. In particular, aspects of the present invention deal with a so-called Evans-type three-phase three-legged wound core in which two adjacent inner cores are enclosed in one outer core, as illustrated in
While requirements for transformer cores range widely, low iron loss is particularly important. From this point of view, low iron loss is an important requirement of grain-oriented electrical steel sheets that are iron core materials. High magnetic flux density is also necessary in order to lower the excitation current in a transformer and to reduce the copper loss. The magnetic flux density is evaluated as the magnetic flux density B8 (T) at a magnetizing force of 800 A/m, and the B8 is generally greater with increasing degree of accumulation in Goss orientation. An electrical steel sheet with a high magnetic flux density generally has a small hysteresis loss and is excellent in iron loss characteristics. In order to reduce iron loss, it is important that the crystal orientation of secondary recrystallized grains in steel sheets be highly aligned with the Goss orientation and that impurities in the steel composition be reduced.
Unfortunately, there are limits in controlling the crystal orientation and in reduction of impurities. Thus, a magnetic domain refining technique has been developed. In this technique, nonuniformity is physically introduced to the surface of a steel sheet and the width of magnetic domains is subdivided to reduce the iron loss. For example, Patent Literature 1 and Patent Literature 2 describe heat-resistant magnetic domain refining methods in which linear grooves with a predetermined depth are formed on the surface of a steel sheet. In Patent Literature 1, the grooves are formed with a gear roller. In Patent Literature 2, the linear grooves are formed on the surface of a steel sheet by etching. These techniques are advantageously applicable to wound cores and the like because the magnetic domain refining effects applied to the steel sheet are not lost even when the steel sheet is heat-treated, for example, strain-relief annealed at the time of wound core production.
In order to reduce the transformer iron loss, it is generally considered that the iron loss (material iron loss) of a grain-oriented electrical steel sheet as an iron core material should be reduced. On the other hand, the iron loss in a transformer is frequently higher than the material iron loss. The value of iron loss (transformer iron loss) in a transformer using an electrical steel sheet as an iron core, divided by the iron loss of the material obtained by, for example, the Epstein test is generally called the building factor (BF) or the destruction factor (DF). That is, the BF in a transformer typically exceeds 1. The lowering of BF will lead to a lower transformer iron loss.
As generally known, some factors (BF factors) have been pointed out as responsible for the increase in transformer iron loss in an Evans-type three-phase three-legged wound core over the material iron loss. Such factors are, for example, the occurrence of magnetic flux concentration at an inner core due to the difference in magnetic path length; the local distortion of magnetic flux waveform in an iron core stemming from three-phase excitation; the occurrence of in-plane eddy-current loss at a steel sheet joint; and an increase in iron loss due to strains introduced by working.
The increase in iron loss that is caused by the magnetic flux concentration on the inner side of an iron core due to the difference in magnetic path length will be discussed. In an Evans-type three-phase three-legged wound core, the magnetic flux is concentrated at an inner core because the magnetic path of the inner core is shorter than the magnetic path of the outer core. In general, the iron loss of a magnetic material increases rapidly in a nonlinear manner versus the increase in excitation magnetic flux density as the saturation magnetization is approached. Furthermore, when the magnetic flux is concentrated at an inner core, the magnetization is saturated and the magnetic flux waveform is distorted to cause a further increase in iron loss. Thus, the magnetic flux concentrated at an inner core gives rise to a specific increase in iron loss on the inner side of the iron core, resulting in an increase in iron loss of the whole iron core.
The occurrence of local distortion of magnetic flux waveform in an iron core stemming from three-phase excitation will be discussed.
The generation of in-plane eddy-current loss at a steel sheet joint will be discussed. In general, a transformer wound core has a cut portion for inserting a winding wire. After a winding wire is inserted into the iron core through the cut portion, the steel sheets are joined together while providing lap zones. As illustrated in
Strains introduced by working are a factor that increases the iron loss. Strains introduced by working, such as slitting of steel sheets and bending at the time of iron core production, impair magnetic properties of the steel sheets and increase the iron loss. Incidentally, a wound core is typically annealed at a temperature above the strain relief temperature after production. This annealing is generally called strain relief annealing.
In consideration of the above factors that increase the transformer iron loss, for example, the following measures have been suggested to reduce the transformer iron loss.
Patent Literature 3 discloses an iron core in which the inner peripheral side with a short magnetic path length is constructed by an electrical steel sheet with lower magnetic properties than the outer peripheral side, and the outer peripheral side with a long magnetic path length is constructed by an electrical steel sheet with higher magnetic properties than the inner peripheral side. The disclosure states that the above configuration avoids magnetic flux concentration on the inner peripheral side of the iron core and effectively reduces the transformer iron loss. Furthermore, Patent Literature 3 discloses a three-phase three-legged wound core in which inner cores and an outer core are each made of materials with different magnetic properties, and the materials are arranged on the inner peripheral side and the outer peripheral side so that the magnetic flux on the inner peripheral side will be concentrated. The disclosure states that the above configuration effectively reduces the transformer iron loss.
As disclosed in Patent Literature 3, the transformer characteristics can be efficiently improved by using different materials on the inner peripheral side and the outer peripheral side so as to avoid magnetic flux concentration on the inner peripheral side. However, this approach entails appropriate arrangement of two kinds of materials (steels) with different magnetic properties (iron loss), thus making the transformer design very complicate and significantly deteriorating the productivity.
An object of aspects of the present invention is to provide a three-phase three-legged wound core that attains excellent magnetic properties with low transformer iron loss without using two or more kinds of materials having different magnetic properties.
In order to produce a three-phase three-legged wound core having excellent magnetic properties with low transformer iron loss, the iron core should be designed so as to reduce the magnetic flux concentration at the inner core stemming from the difference in magnetic path length and the iron core material should be selected so that the magnetic flux waveform will not be distorted and the increase in iron loss will be small even when the magnetic flux is concentrated at the inner core. Furthermore, it is also necessary to suppress the local distortion of magnetic flux waveform in the iron core stemming from three-phase excitation.
The iron core design for reducing the magnetic flux concentration requires the following two points:
To suppress the occurrence of local distortion of magnetic flux waveform in an iron core stemming from three-phase excitation, the following design is needed.
To realize a small increase in iron loss even when the magnetic flux waveform is distorted, the iron core material that is selected preferably satisfies the following:
In the above formula, the iron loss under harmonic superposition and the iron loss without harmonic superposition are the iron loss (W/kg) each measured under the condition of a frequency of 50 Hz and a maximum magnetization of 1.7 T, and the iron loss under harmonic superposition is the iron loss measured under conditions where the superposition ratio of third harmonic to fundamental harmonic at an excitation voltage is 40% and the phase difference is 60°.
These requirements and the reasons why these conditions are required will be described in detail below.
The wound core is produced by winding a magnetic material, such as a grain-oriented electrical steel sheet. In a typical method for wound core production, a steel sheet is wound into a cylindrical shape and is pressed into a rectangular shape so that corner sections will have a predetermined curvature. In an alternative production method, portions that will be corner sections of a wound core are bent beforehand, and the bent steel sheets are stacked to form a wound core. An iron core formed by this method has bends (bent portions) at the corner sections. Iron cores formed by the former method are generally called tranco-cores, and iron cores formed by the latter method are generally referred to as unicores or duocores depending on the number of steel sheet joints provided. The latter method that forms bends (bent portions) at corner sections is suited for reducing the magnetic flux concentration.
The results of experimental investigation of the magnetic flux concentration and the magnetic flux density waveform in tranco-cores and unicores are discussed below. One tranco-core and two unicores of three-phase three-legged type, having the shapes illustrated in
The distortion of magnetic flux waveform is suppressed by the unicore design, specifically, by providing bent portions at corner sections of an iron core, probably for the following reason. Deformation twins and the like remain in bent portions of corner sections of a unicore even when strain relief annealing is performed, and the magnetic permeability is locally reduced compared to other portions. Such portions with extremely low magnetic permeability do not allow the passage of magnetic flux above a certain level. As a result, the magnetic flux will not be concentrated exclusively on the inner side of the iron core even in the presence of a difference in magnetic path length. When magnetic flux concentration occurs, the magnetic flux is saturated at a portion where the magnetic flux density is maximum. Thus, as illustrated in
Aspects of the present invention are directed to a three-phase three-legged wound core having bent portions at corner sections. For example, the wound core is composed of two adjacent inner cores and one outer core enclosing the two inner cores, similarly to the unicore illustrated in
The results of experimental investigation of the influences of the magnetic flux density B8 on the distortion of magnetic flux waveform in a unicore will be discussed. Three-phase three-legged unicores (two inner cores and one outer core) having the shape illustrated in
The magnetic flux concentration at the inner core is relaxed with increasing magnetic flux density B8 of the grain-oriented electrical steel sheet as the material forming the iron core. The reason behind this is probably as follows. An iron core material having a high magnetic flux density B8 is generally slow in reaching magnetic flux saturation. Even when the magnetic flux is concentrated on the inner side of an iron core due to the difference in magnetic path length, saturation does not occur until a high magnetic flux density is reached and thus the trapezoidal distortion of magnetic flux waveform will be unlikely to occur. If, on the other hand, the magnetic flux density B8 of an iron core material is too high, the highness in saturation magnetization allows the magnetic flux to be concentrated excessively in the presence of a difference in magnetic path length, thus leading to a large distortion of magnetic flux waveform. The present inventors assume that the distortion of magnetic flux waveform could be reduced to a low level in a certain range of the magnetic flux density B8.
The following describes the iron core shape design and the reasons why the iron core shape is thus designed to suppress the occurrence of local distortion of magnetic flux waveform in the iron core stemming from three-phase excitation.
As described hereinabove, when a magnetic flux is caused to flow by three-phase excitation, part of the magnetic flux flows into the leg with zero excitation (the right leg in
The above hypothesis was verified by experiments as described below. As illustrated in
Next, the conditions and the reasons will be described for the selection of an iron core material that has a small increase in iron loss even when a distortion of magnetic flux waveform occurs.
As already described, magnetic flux concentration on the inner side of an iron core distorts the magnetic flux waveform into trapezoidal and results in an increase in iron loss. The reason behind this is that when the magnetic flux waveform is trapezoidal, a sharp change occurs in the magnetic flux at a moment on a side of the trapezoid and consequently the eddy-current loss is increased. A sharp change in magnetic flux occurs similarly when the magnetic flux waveform in an iron core is locally distorted upon three-phase excitation, and consequently the eddy-current loss is increased.
In order to simulate the distortion of magnetic flux waveform and the increase in eddy-current loss, iron core materials were magnetically tested while the magnetic flux waveform was intentionally distorted by harmonic superposition. The test was performed under various harmonic superposition conditions. The results have shown that the increase in eddy-current loss in a wound core is well simulated by the iron loss measured under conditions where the superposition ratio of third harmonic to fundamental harmonic at an excitation voltage is 40% and the phase difference is 60°.
The experimental results that support the above preferred range will be discussed below. Three-phase three-legged unicores (two inner cores and one outer core) having the shape illustrated in
By selecting the iron core material based on the iron loss deterioration rate under harmonic superposition, the increase in iron loss can be better suppressed even when a distortion of magnetic flux waveform occurs.
Aspects of the present invention have been made based on the findings discussed above and include the following configurations.
[1] A three-phase three-legged wound core comprising two adjacent inner cores and one outer core enclosing the two inner cores, the inner cores and the outer core comprising a grain-oriented electrical steel sheet, wherein
[2] The three-phase three-legged wound core according to [1], wherein the grain-oriented electrical steel sheet has an iron loss deterioration rate under harmonic superposition of 1.35 or less as determined from the following formula:
iron loss deterioration rate under harmonic superposition=(iron loss under harmonic superposition)/(iron loss without harmonic superposition)
wherein the iron loss under harmonic superposition and the iron loss without harmonic superposition are each an iron loss (W/kg) measured at a frequency of 50 Hz and a maximum magnetization of 1.7 T, and the iron loss under harmonic superposition is an iron loss measured under conditions where the superposition ratio of third harmonic to fundamental harmonic at an excitation voltage is 40% and the phase difference is 60°.
[3] The three-phase three-legged wound core according to [1] or [2], wherein the grain-oriented electrical steel sheet has been subjected to non-heat-resistant magnetic domain refining treatment.
[4] A method for producing a three-phase three-legged wound core, the three-phase three-legged wound core being such that the three-phase three-legged wound core comprises two adjacent inner cores and one outer core enclosing the two inner cores; the inner cores and the outer core comprise a grain-oriented electrical steel sheet; and the two inner cores and the one outer core each have a flat section, a corner section adjacent to the flat section, a lap zone in the flat section, and a bent portion in the corner section, the method comprising:
[5] The method for producing a three-phase three-legged wound core according to [4], wherein the grain-oriented electrical steel sheet has an iron loss deterioration rate under harmonic superposition of 1.35 or less as determined from the following formula:
iron loss deterioration rate under harmonic superposition=(iron loss under harmonic superposition)/(iron loss without harmonic superposition)
[6] The method for producing a three-phase three-legged wound core according to [4] or [5], wherein the grain-oriented electrical steel sheet has been subjected to non-heat-resistant magnetic domain refining treatment.
The three-phase three-legged wound core provided according to aspects of the present invention has low transformer iron loss and excels in magnetic properties. According to aspects of the present invention, a three-phase three-legged wound core having excellent magnetic properties with low transformer iron loss can be obtained without using two or more kinds of materials having different magnetic properties (iron loss). Aspects of the present invention can reduce the complexity encountered when designing iron cores using two or more kinds of materials having different magnetic properties, for example, the arrangement of such materials, and enable high productivity of iron cores having excellent magnetic properties with low iron loss.
Embodiments of the present invention will be described in detail below.
As described above, the following conditions should be satisfied in order to achieve a transformer wound core with low iron loss.
The condition (A) is satisfied by adopting a technique for producing a transformer wound core generally called a unicore or duocore type. Specifically, the condition (A) is satisfied by, as already described, constructing a three-phase three-legged wound core in such a manner that two adjacent inner cores and one outer core enclosing the two inner cores are each provided with a flat section, a corner section adjacent to the flat section, a lap zone in the flat section, and a bent portion in the corner section. The wound core may be produced by a known method. More specifically, for example, a unicore producing machine manufactured by AEM Cores Pty Ltd. may be used. In this case, the machine that has been loaded with the design size shears and bends a steel sheet to the designed size, thereby giving worked steel sheets one by one, and the worked steel sheets are stacked together to form the wound core.
In the condition (B), the bent portion indicates a portion in the corner section where the steel sheet changes its winding direction as viewed from the side of the iron core (viewed from the side in relation to the direction in which the steel sheet is wound). The angle formed by two bent portions is defined as the smaller angle (the angle less than) 180° of the angles formed by the two bent portions in one corner section (see
As long as the requirements (A) and (B) are controlled within the ranges according to aspects of the present invention, conditions other than (A) and (B), such as the type of steel sheet joints, and the iron core size, are not particularly limited.
As described above, it is necessary to satisfy the condition (C) below in order to achieve a three-phase three-legged transformer wound core with low iron loss. Furthermore, it is preferable to satisfy the condition (D) below. (C) The grain-oriented electrical steel sheet as the iron core material has a magnetic flux density B8 of 1.92 T or more and 1.98 T or less at a magnetic field strength H of 800 A/m.
The magnetic properties are measured by the Epstein test. The Epstein test is performed in a known manner, such as IEC standards or JIS standards. When it is difficult to evaluate the magnetic flux density B8 by the Epstein test, for example, in the case of a non-heat-resistant magnetic domain refined material, the results obtained with a single sheet tester (SST) may be used instead. In the wound core production, the selection of materials according to the suitable range of magnetic flux density B8 should be made based on the representative properties of the grain-oriented electrical steel sheet coils. Specifically, test samples are collected from the front and rear ends of the steel sheet coil and are subjected to the Epstein test to measure the magnetic flux density B8, and the results are averaged to give the representative properties. Alternatively, the materials may be selected based on the property values (the average value and the guaranteed value) of the steel sheets provided by the steel manufacturers. The magnetic flux density B8 is preferably 1.94 T or more. The magnetic flux density B8 is preferably 1.96 T or less.
iron loss deterioration rate under harmonic superposition=(iron loss under harmonic superposition)/(iron loss without harmonic superposition).
The iron loss under harmonic superposition and the iron loss without harmonic superposition defined in the above formula are the iron loss (W/kg) measured at a frequency of 50 Hz and a maximum magnetization of 1.7 T using the same Epstein tester or the same single sheet tester, and the iron loss under harmonic superposition is the iron loss measured under conditions where the superposition ratio of third harmonic to fundamental harmonic at an excitation voltage is 40% and the phase difference is 60°. The harmonic is superimposed on the voltage applied to the primary winding wire. The harmonic may be superimposed on the voltage applied to the primary winding wire in any manner without limitation. For example, a voltage with harmonic superposed waveform may be generated with a waveform generator and may be amplified with a power amplifier to serve as the excitation voltage (the voltage applied to the primary winding wire). In the harmonic superposition conditions in accordance with aspects of the present invention, the superposition ratio of third harmonic to fundamental harmonic at the excitation voltage is 40% and the phase difference is 60°. That is, the voltage waveform under the harmonic superposition conditions in accordance with aspects of the present invention is created by superposing, on a 50-Hz sine wave as the fundamental harmonic, the third harmonic, namely, a 150-Hz sine wave with 40% amplitude of the fundamental harmonic amplitude and a delay (a phase difference) of 60°. In accordance with aspects of the present invention, as described above, it is preferable that the grain-oriented electrical steel sheet used as the iron core material have an iron loss deterioration rate under harmonic superposition of 1.35 or less. The iron loss deterioration rate under harmonic superposition is more preferably 1.15 or less. The lower limit of the iron loss deterioration rate under harmonic superposition is not particularly limited. As an example, the iron loss deterioration rate under harmonic superposition is 1.00 or more.
As long as the requirement (C) is controlled to the range according to aspects of the present invention, conditions other than (C), such as characteristics, components, and production method, of the grain-oriented electrical steel sheet are not particularly limited.
In accordance with aspects of the present invention, the control of the requirements (A) to (C) to the ranges according to aspects of the present invention allows a three-phase three-legged wound core to attain excellent magnetic properties with low transformer iron loss without using two or more kinds of materials having different magnetic properties. Thus, aspects of the present invention can reduce the complexity encountered when designing iron cores using two or more kinds of iron core materials having different magnetic properties, for example, the arrangement of such materials, and enables high productivity of three-phase three-legged wound cores having excellent magnetic properties with low iron loss.
Components and a method of production of a grain-oriented electrical steel sheet suited as the material for the three-phase three-legged wound core according to aspects of the present invention will be described below.
In accordance with aspects of the present invention, the chemical composition of a slab for grain-oriented electrical steel sheet may be any chemical composition as long as secondary recrystallization occurs. An inhibitor may be used. When, for example, an AlN inhibitor is used, appropriate amounts of Al and N may be added. When a MnS. MnSe inhibitor is used, appropriate amounts of Mn and Se and/or S may be added. It is needless to mention that both inhibitors may be used in combination. In such a case, the Al, N, S, and Se contents are preferably Al: 0.010 to 0.065 mass %, N: 0.0050 to 0.0120 mass %, S: 0.005 to 0.030 mass %, and Se: 0.005 to 0.030 mass %.
Aspects of the present invention may also be applied to an inhibitor-free grain-oriented electrical steel sheet in which the Al, N, S, and Se contents are limited. In this case, the amounts of Al, N, S, and Se are preferably controlled to Al: 100 ppm by mass or less, N: 50 ppm by mass or less, S: 50 ppm by mass or less, and Se: 50 ppm by mass or less.
The basic components and optional components of the slab for grain-oriented electrical steel sheet are described in detail below.
Carbon is added to improve the microstructure of the hot-rolled sheet. If, however, the C content is more than 0.08 mass %, it is difficult to decarburize the steel to a level of 50 ppm by mass or less where magnetic aging does not occur, before the completion of the production process. Thus, the C content is preferably 0.08 mass % or less. The C content has no particular lower limit because secondary recrystallization can occur even in a material containing no carbon. That is, the C content may be 0 mass %.
Silicon is an element effective in increasing the electrical resistance of steel and improving the iron loss. When the Si content is 2.0 mass % or more, the iron loss lowering effects are enhanced. When, on the other hand, the Si content is 8.0 mass % or less, the decrease in workability can be controlled easily and the decrease in magnetic flux density can also be controlled easily. Thus, the Si content is preferably in the range of 2.0 to 8.0 mass %.
Manganese is an element necessary to improve hot workability. The addition produces its effect easily when the Mn content is 0.005 mass % or more. When, on the other hand, the Mn content is 1.000 mass % or less, the decrease in magnetic flux density of product sheets can be controlled easily. Thus, the Mn content is preferably in the range of 0.005 to 1.000 mass %.
Chromium is an element that promotes the formation of a dense oxide film at the interface between a forsterite film and the steel substrate. Although an oxide film can form even in the absence of chromium, for example, the addition of 0.02 mass % or more chromium is expected to expand the preferred ranges of other components. When the Cr content is 0.20 mass % or less, an excessive increase in oxide film thickness can be prevented and the coating will be more resistant to separation. Thus, the Cr content is preferably in the range of 0.02 to 0.20 mass %.
The slab for grain-oriented electrical steel sheet preferably has the components described above as the basic components. In addition to the basic components, the slab may appropriately contain the following elements.
At least one selected from Ni: 0.03 to 1.50 mass %, Sn: 0.010 to 1.500 mass %, Sb: 0.005 to 1.500 mass %, Cu: 0.02 to 0.20 mass %, P: 0.03 to 0.50 mass %, and Mo: 0.005 to 0.100 mass %
Nickel is an element that is useful for improving the microstructure of the hot-rolled sheet and enhancing magnetic properties. When the Ni content is 0.03 mass % or more, magnetic properties are enhanced more effectively. When the Ni content is 1.50 mass % or less, the destabilization of secondary recrystallization can be suppressed and the risk will be reduced of the magnetic properties of product sheets being deteriorated. Thus, when nickel is added, the Ni content is preferably in the range of 0.03 to 1.50 mass %.
Tin, antimony, copper, phosphorus, and molybdenum are elements useful for enhancing magnetic properties, and offer effective enhancements in magnetic properties more easily when added at or above the lower limit contents of the respective elements. On the other hand, these elements added at or below the upper limit contents will not increase the risk that the development of secondary recrystallized grains will be inhibited. Thus, when tin, antimony, copper, phosphorus, and molybdenum are added, the contents of the respective elements are preferably within the ranges described above.
The balance after the above components is incidental impurities mixed during the production process and iron.
Next, a method for producing a grain-oriented electrical steel sheet suited as the material for the three-phase three-legged wound core according to aspects of the present invention will be described.
A slab with the chemical composition described above is heated in a usual manner. The heating temperature is preferably 1150 to 1450° C.
The heating is followed by hot rolling. Hot rolling may be performed directly after casting without heating. Hot rolling may be performed or omitted for a thin cast steel. When hot rolling is performed, the rolling temperature in the final rough rolling pass is preferably 900° C. or above, and the rolling temperature in the final finish rolling pass is preferably 700° C. or above.
Subsequently, the hot-rolled sheet is annealed as required. In order to highly develop the Goss texture in the product sheet, the annealing temperature for the hot-rolled sheet is preferably in the range of 800 to 1100° C. If the annealing temperature for the hot-rolled sheet is below 800° C., the band texture formed in the hot rolling remains to make it difficult to realize a primary recrystallization texture with a controlled grain size, thus causing a risk that the development of secondary recrystallized grains will be inhibited. If, on the other hand, the annealing temperature for the hot-rolled sheet is above 1100° C., the grains after the hot-rolled sheet annealing are so coarsened that it may be difficult to realize a primary recrystallization texture with a controlled grain size.
Subsequently, cold rolling is performed once, or two or more times with intermediate annealing. The intermediate annealing temperature is preferably 800° C. or above and 1150° C. or below. The intermediate annealing time is preferably about 10 to 100 seconds.
Subsequently, decarburization annealing is performed. In the decarburization annealing, the annealing temperature is preferably 750 to 900° C., the oxidizing atmosphere PH2O/PH2 is preferably 0.25 to 0.60, and the annealing time is preferably about 50 to 300 seconds.
Subsequently, an annealing separator is applied. The annealing separator is preferably one based on MgO and the amount of application is preferably about 8 to 15 g/m2.
Subsequently, finish annealing is performed for the purposes of secondary recrystallization and forming a forsterite film. The annealing temperature is preferably 1100° C. or above, and the annealing time is preferably 30 minutes or more.
Subsequently, flattening treatment (flattening annealing) and insulating coating treatment are performed. The shape may be corrected concurrently in the insulating coating treatment by flattening the steel by the baking of the insulating coating that has been applied. The flattening annealing is preferably performed at an annealing temperature of 750 to 950° C. for an annealing time of about 10 to 200 seconds. In accordance with aspects of the present invention, the insulating coating may be applied to the surface of the steel sheet before or after the flattening annealing. Here, the insulating coating is a coating that applies a tension to the steel sheet (a tension coating) in order to reduce the iron loss. For example, the tension coating may be an inorganic coating containing silica, or a ceramic coating by physical vapor deposition, chemical vapor deposition, or the like.
In general, the iron loss deterioration rate under harmonic superposition decreases with increasing tension force on the steel sheet applied by the surface film (the forsterite film and the insulating coating). While the film tension can be increased by increasing the thickness of the tension coating, the space factor may be deteriorated. In the case of an inorganic coating containing silica, for example, the baking temperature may be increased and thereby glass crystallization may be promoted in order to obtain high tension without deteriorating the space factor. High tension is effectively obtained also by the application of a film with a low thermal expansion coefficient, such as a ceramic coating.
To reduce the iron loss of the steel sheet, magnetic domain refining treatment is preferably performed. The magnetic domain refining technique reduces the iron loss by subdividing the width of magnetic domains through the physical introduction of nonuniformity to the surface of the steel sheet. The magnetic domain refining technique is broadly classified into heat-resistant magnetic domain refinement that does not lose the effect upon strain relief annealing, and non-heat-resistant magnetic domain refinement that loses the effect upon strain relief annealing. Aspects of the present invention may be applied to any of steel sheets without magnetic domain refining treatment, steel sheets with heat-resistant magnetic domain refining treatment, and steel sheets with non-heat-resistant magnetic domain refining treatment.
In particular, aspects of the present invention are suitably applied to a steel sheet with non-heat-resistant magnetic domain refining treatment rather than a steel sheet with heat-resistant magnetic domain refining treatment. The non-heat-resistant magnetic domain refining treatment is typically a treatment that divides magnetic domains into smaller domains by irradiating the steel sheet after secondary recrystallization with a high-energy beam (such as a laser beam) to introduce high-dislocation density regions into the steel sheet surface layer and thereby to form associated stress fields. In the non-heat-resistant magnetic domain refined material (the steel sheet with non-heat-resistant magnetic domain refining treatment), an increase in eddy-current loss by harmonic superposition can be avoided by virtue of the high tensile stress fields formed by the introduction of high-dislocation density regions into the steel sheet uppermost layer. The non-heat-resistant magnetic domain refining treatment may be performed by a known technique, such as applying a high-energy beam (such as a laser beam, an electron beam, or plasma jet) to the steel sheet surface.
Aspects of the present invention will be described in detail based on Examples. The following Examples are only illustrative of preferred modes of the present invention and do not in any way limit the scope of the present invention. The embodiments of the present invention may be modified appropriately within the scope of the gist of the present invention, and all such modifications are included in the technical scope of the present invention.
Three-phase three-legged tranco-cores and unicores with the iron core shapes described in
The results are described in Table 6. It has been shown that superior magnetic properties were obtained in Examples and Optimum Examples of the present invention, with lower transformer iron loss and lower BF than Comparative Examples. In particular, Optimum Examples that involved a non-heat-resistant magnetic domain refined material with an iron loss deterioration rate under harmonic superposition of 1.35 or less attained very low transformer iron loss.
1.90
1.90
1.88
1.90
57
57
1.88
57
63
68
1.91
1.99
57
63
1.90
1.91
1.99
| Number | Date | Country | Kind |
|---|---|---|---|
| 2022-032471 | Mar 2022 | JP | national |
This is the U.S. National Phase application of PCT/JP2023/005716, filed Feb. 17, 2023 which claims priority to Japanese Patent Application No. 2022-032471, filed Mar. 3, 2022, the disclosures of these applications being incorporated herein by reference in their entireties for all purposes.
| Filing Document | Filing Date | Country | Kind |
|---|---|---|---|
| PCT/JP2023/005716 | 2/17/2023 | WO |
