AMORPHOUS Fe-B-Si-C ALLOYS HAVING SOFT MAGNETIC CHARACTERISTICS USEFUL IN LOW FREQUENCY APPLICATIONS

Abstract: A rapidly solidified amorphous metallic alloy is composed of iron, boron, silicon and carbon. The alloy exhibits in combination high saturation induction, high Curie temperature, high crystallization temperature, low core loss and low exciting power at line frequencies and is particularly suited for use in cores of transformers for an electrical power distribution network.

Description: Amorphous Fe-B-Si-C Alloys Having Soft Magnetic Characteristics Useful in Low Frequency Applications Background of the Invention Cross Reference To Related Applications This is a continuation-in-part of U. S. Application Serial No. 08/647, 151, filed May 9, 1996 which, in turn, is a file- wrapper continuation of U. S. Application Serial No. 08/246,393, filed May 20, 1994 which, in turn, is a file-wrapper continuation of U.S. Application Serial No. 996,288, filed December 23, 1992. 1. Field of the Invention This invention relates to amoφhous metallic alloys, and more particularly to amoφhous alloys consisting essentially of iron, boron, silicon, and carbon which find uses in the production of magnetic cores used in the manufacture of electric distribution and power transformers. 2. Description of the Prior Art Amoφhous metallic alloys (metallic glasses) are metastable materials lacking any long range atomic order. They are characterized by x-ray diflfraction patterns consisting of diffuse (broad) intensity maxima, quantitatively similar to the diffraction patterns observed for liquids or inorganic oxide glasses. However, upon heating to a sufficiently high temperature, they begin to crystallize with the evolution of the heat of crystallization. Correspondingly, the x-ray diffraction pattern begins to change to that observed from crystalline materials, i.e., shaφ intensity maxima begin to evolve in the pattern. The metastable state of these alloys offers significant advantages over the crystalline forms of the same alloys, particularly with respect to the mechanical and magnetic properties of the alloy. For example, there are commercially available metallic glasses which have only about a third of the total core losses of those of conventional crystalline 3 wt.% Si-Fe grain-oriented steels, in applications as magnetic cores of electrical distribution transformers. (See, for example "Metallic Glasses in Distribution Transformer Applications: An Update", by V.R.V. Ramanan, J. Mater. Eng., U, (1991) pp. 1 19- 127). Considering that there are about 30 million distribution transformers in the U.S. alone, which consume about 5 billion pounds of magnetic core material, the potential for energy savings and the associated economic benefits resulting from the use of metallic glasses in distribution transformer cores can be substantial. Amoφhous metallic alloys are produced generally by rapidly cooling a melt using any of a variety of techniques conventional in the art. The term "rapid cooling" usually refers to cooling rates of at least about 10 °C/s; in the case of most Fe-rich alloys, generally higher cooling rates (10 to 10 °C/s) are necessary to suppress the formation of crystalline phases, and to quench the alloy into the metastable amoφhous state. Examples of the techniques available for fabricating amoφhous metallic alloys include sputter or spray depositing onto a (usually chilled) substrate, jet casting, planar flow casting, etc. Typically, the particular composition is selected, powders or granules of the requisite elements (or of materials that decompose to form the elements, such as ferroboron, ferrosilicon, etc.) in the desired proportions are then melted and homogenized and the molten alloy is then rapidly quenched at a rate appropriate, for the chosen composition, to the formation of the amoφhous state. The most preferred process for fabricating continuous metallic glass strip is the process known as planar flow casting, set forth in USP 4, 142,571 to Narasimhan, assigned to AlliedSignal Inc. The planar flow casting process comprises the steps of: (a) moving the surface of a chill body in a longitudinal direction at a predetermined velocity of from about 100 to about 2000 meters per minute past the orifice of a nozzle defined by a pair of generally parallel lips delimiting a slotted opening located proximate to the surface of the chill body such that the gap between the lips and the surface changes from about 0.03 to about 1 millimeter, the orifice being arranged generally peφendicular to the direction of movement of the chill body, and (b) forcing a stream of molten alloy through the orifice of the nozzle into contact with the surface of the moving chill body to permit the alloy to solidify thereon to form a continuous strip. Preferably, the nozzle slot has a width of from about 0.3 to 1 millimeter, the first lip has a width at least equal to the width of the slot and the second lip has a width of from about 1.5 to 3 times the width of the slot. Metallic strip produced in accordance with the Narasimhan process can have widths ranging from 7 millimeters, or less, to 150 to 200 mm, or more. The planar flow casting process described in USP 4, 142,571 is capable of producing amoφhous metallic strip ranging from less than 0.025 millimeters in thickness to about 0.14 millimeters or more, depending on the composition, melting point, solidification and crystallization characteristics of the alloy employed. Understanding which alloys can be produced economically and in large quantities in the amoφhous form and the properties of alloys in the amoφhous form has been the subject of considerable research over the past 20 years. The most well- known disclosure directed to the issue - What alloys can be more easily produced in the amoφhous form? - is USP Re 32,925 to H.S. Chen and D.E. Polk, assigned to AlliedSignal Inc. Disclosed therein is a class of amoφhous metallic alloys having the formula M a YbZ c , where M is a metal consisting essentially of a metal selected from the group of iron, nickel, cobalt, chromium, and vanadium, Y is at least one element selected from the group of phosphorus, boron and carbon, Z is at least one element form the group consisting of aluminum, antimony, beryllium, germanium, indium, tin and silicon, "a" ranges from about 60 to 90 atom %, "b" ranges from about 10 to 30 atom % and "c" ranges from about 0.1 to 15 atom percent. Today, the vast majority of commercially available amoφhous metallic alloys are within the scope of the above-recited formula. With continuing research and development in the area of amoφhous metallic alloys, it has become apparent that certain alloys and alloy systems possess magnetic and physical properties which enhance their utility in certain applications of worldwide importance, particularly in electrical applications as core materials for distribution and power transformers, generators and electric motors. Early research and development in the area of amoφhous metallic alloys identified a binary alloy, Fe8oB20 > as a candidate alloy for use in the manufacture of magnetic cores employed in transformers, particularly distribution transformers, and generators because the alloy exhibited a high saturation magnetization value (about 178 emu/g). It is known, however, that FesoB20 is difficult to cast into amoφhous form. Moreover, it tends to be thermally unstable because of a low crystallization temperature and is difficult to produce in ductile strip form. Further, it has been determined that its core loss and exciting power requirements are only minimally acceptable. Thus, alloys of improved castability and stability, and improved magnetic properties, had to be developed to enable the practical use of amoφhous metallic alloys in the manufacture of magnetic cores, especially magnetic cores for distribution transformers. Subsequent to additional research, ternary alloys of Fe-B-Si were identified as superior to FesoB20 for use in such applications. A wide range of alloy classes, with their own unique set of magnetic properties, have been disclosed over the years. USP's 4,217,135 and 4,300,950 to Luborsky et al. disclose a class of alloys represented generally by the formula Feso-84Bi2-19Sii-8 subject to the provisos that the alloy must exhibit a saturation magnetization value of at least about 174 emu/g (a value presently recognized as the preferred value) at 30°C, a coercivity less than about 0.03 Oe and a crystallization temperature of at least about 320°C. Freilich et al. in U.S. Patent Application Serial No. 220,602, assigned to AlliedSignal Inc., disclosed that a class of Fe-B-Si alloys represented by the formula Fe~75_ 78.5B-1 l~2lSi~4~10.5 exhibited high crystallization temperature combined with low core loss and low exciting power requirements at conditions approximating the ordinary transformer operating conditions of magnetic cores in distribution transformers (i.e. 60 Hz, 1.4 T at 100°C), while maintaining acceptably high saturation magnetization values. Canadian Patent No. 1 , 174,081 discloses that a class of alloys defmed by the formula Fe77_8θBi2-16Si5-10 exhibit low core loss and low coercivity at room temperature after aging, and have high saturation magnetization values. In USP 5,035,755, assigned to AlliedSignal Inc., Nathasingh et al. disclose a class of alloys useful for manufacture of magnetic cores for distribution transformers, which are represented by the formula Fe794.79 %B \ 2- 14Siό-8 > and which alloys exhibit unexpectedly low core loss and exciting power requirements both before and after aging, in combination with an acceptably high saturation magnetization value. Finally, U.S. P. 5,496,418 to Ramanan et al., assigned to AlliedSignal Inc., disclosed yet another class of Fe-B-Si alloys with high iron contents exhibiting improved utility and handleability in the production of magnetic cores used in the manufacture of electric distribution and power transformers. It is disclosed that these alloys have the combination of high crystallization temperature, high saturation induction, low core loss and low exciting power requirements at 60 Hz and 1.4 T at 25°C over a range of annealing conditions, and improved retention of ductility subsequent to anneals over a range of annealing conditions. In other research efforts to redress the deficient characteristics in Fe8oB20, and to recover some of the saturation magnetization "lost" from the Fe-B system, the ternary Fe-B-C alloys were taught to have great promise. The properties of alloys in this system are summarized in a comprehensive report by Luborsky et al. in "The Fe-B-C Ternary Amoφhous Alloys", General Electric Co. Technical Information Series Report No. 79CRD169, August 1979. It is disclosed in this report that while a high saturation magnetization value persists over a wider range of compositions in the Fe-B-C system when compared with the Fe-B-Si system, the beneficial effects found from Si (in Fe-B-Si alloys) on increased crystallization temperatures, and, therefore, alloy stability, were seriously compromised over much of the composition region in the Fe-B-C alloys. In other words, crystallization temperatures usually were reduced when C replaced B. From a magnetic property perspective, a major drawback noted from the Fe-B-C alloys was that the coercivities of these alloys were higher than those of the Fe-B-Si alloys and higher, even, than that of the binary Fe-B alloy. Primarily as a result of these deficiencies in alloy stability and coercivity, the Fe-B-C alloys have not been pursued further, since the time of the Luborsky et al. report, as possible commercially significant alloys for application in magnetic cores of transformers for electrical distribution. A class of amoφhous metallic Fe-B-Si-C alloys represented by the formula Fe8θ-82Bl2.5-14.5Si2.5-5.θCi.5-2.5 are disclosed by DeCristofaro et al. in USP 4,219,355, assigned to AlliedSignal Inc., which alloys are disclosed to exhibit, in combination, high magnetization, low core loss and low volt-ampere demand (at 60 Hz), and wherein the improved ac and dc magnetic characteristics remain stable at temperatures up to 150°C. DeCristofaro et al. also disclose that Fe-B-Si-C alloy compositions outside of the above formula possess unacceptable dc characteristics (coercivity, Bso (induction at 1 Oe), etc.), or ac characteristics (core loss and/or exciting power), or both. Amoφhous metallic Fe-B-Si-C alloys are also disclosed in USP 4,437,907 to Sato et al. In this patent, it is taught that there is a class of alloys described by the formula Fe74-8θB6-13Si8-19Cθ-3 . 5, which alloys exhibit a low core loss at 50 Hz and 1.26 T and high thermal stability of magnetic properties, and in which alloys, there is, after aging at 200°C, a high degree of retention of magnetic flux density measured at 1 Oe at room temperature and a good degree of retention of core loss at the above mentioned conditions. USP 4,865,664 to Sato et al. discloses an iron base amoφhous alloy having a sheet thickness of from 50 to 150 μm and a sheet width of at least 20 mm. The strip is produced by a single-roller cooling process and has a fracture strain of 0.01 or more. Sato et al. '664 further discloses an amoφhous alloy strip composed of Fe,BbSicCd in which the ranges of a, b, c, and d are preferably 77 to 82, 8 to 15, 4 to 15, and 0 to 3, respectively. Japanese Patent Publication 37,467 (August 7, 1989) discloses a low iron loss, iron-based amoφhous alloy which has the composition Fe»SibB c Ca and which has a very small change of magnetic properties with time. The values of a, b, c, and d are in atom percent, a = 77 - 79, b = over 8 to 12, c = 9 - 11, and d = 1 - 3, and a+b+c+d=100. Japanese Kokai Publication 33,452 (April 3, 1981) discloses an amoφhous alloy for use in the iron core of a transformer having the composition Fe a SibB c Cd in which values of a, b, c, and d are in atom percent, a + b + c + d = 100, with b = 2 - 8, c = 8 - 17, and d = 1 - 8. Japanese Kokai Publication 34, 162 (February 28, 1983) discloses an amoφhous alloy of formula Fe j BpSi Cj. The values of a, b, c, and d are in atom percent, a + b + c + d = 100, and a = 78-82, b = 8-14, c = 5-15, and d < 1.5, the alloy having good resistance to magnetic aging. Japanese Kokai Publication 152,150 (November 27, 1980) discloses a high magnetic flux density amoφhous iron alloy which contains, in atom percent, 1 1-17% boron and 3-8% carbon and the remainder consisting substantially of iron, the alloy having a high magnetic permeability and a small iron loss. This document also discloses a high magnetic flux density amoφhous iron alloy which contains, in atom percent, 11-17% boron and 3-8% carbon, at least one of less than 5% of the former and less than 8% of the latter being substituted with silicon, the sum of silicon, boron and carbon being 18-21%, and the remainder consisting substantially of iron, the alloy having a high magnetic permeability and a small iron loss. It is readily apparent from the above discussion that researchers focused on different properties as being critical to the determination of which alloys would be best suited for the manufacture of magnetic cores for distribution and power transformers, but none recognized the combination of properties necessary for clearly superior results in all aspects of the production and operation of magnetic cores and, consequently, a variety of different alloys were discovered, each focusing on only part of the total combination. More specifically, conspicuously absent from the above recited disclosures is an appreciation for a class of alloys wherein the alloys exhibit a high crystallization temperature and a high saturation magnetization value, in combination with low core loss and low exciting power requirements after having been annealed over a wide range of annealing temperatures and times and, in addition, retain sufficient ductility over a range of annealing conditions to ease magnetic core production. Alloys which exhibit this combination of features would find overwhelming acceptance in the transformer manufacturing industry because they would possess the magnetic characteristics essential to improved operation of the transformer and more readily accommodate variations in the equipment, processes and handling techniques employed by different transformer core manufacturers. The element boron in the amoφhous metallic alloys discussed above is the major cost component in the total raw material costs associated with these alloys. For example, in the case of the Fe-B-Si alloys discussed above, 3 percent by weight (about 13 at.%) of boron in an alloy could represent as much as about 70% of the total raw material costs. In addition to the desirable combination of features described above for a transformer core alloy, if such an alloy could have lower boron levels in its composition, thereby allowing reduced total production costs in large scale manufacture of the alloy for transformer applications, a more rapid implementation of amoφhous metallic alloy cores would occur, with the attendant societal benefits discussed previously. Summary of the Invention The present invention provides novel metallic alloys composed of iron, boron, silicon, and carbon, which are at least about 70% amoφhous, and which consist essentially of the composition Fe a B D Si c Cd, wherein "a" - "d" are in atomic percent, the sum of "a", "b", "c", and "d" equals 100, "a" ranges from about 77 to 80, b" ranges from about 7 to 11.5, "c" ranges from about 3 to 12, and "d" ranges from about 2 to 6, with the proviso that when "c" is greater than 7.5 "d" is at least 4, the metallic alloys having up to about 0.5 atomic percent of impurities and having a crystallization temperature of at least 500°C. The alloys of this invention evidence, in combination, a Curie temperature of at least about 360°C, a saturation magnetization corresponding to a magnetic moment of at least about 165 emu/g and, a core loss not greater than about 0.35 W kg and an exciting power value not greater than about 1 VA/kg, when measured at 25°C, 60 Hz and 1.4 T, after the alloys have been annealed at a temperature within the range of 335°C-390°C, for a time ranging between 0.5 and 4 hours, in the presence of a magnetic field in the range of 5-3 O Oe. The present invention also provides an improved magnetic core comprised of the amoφhous metallic alloys of the invention. The improved magnetic core comprises a body (e. g., wound, wound and cut, or stacked) consisting essentially of amoφhous metallic alloy ribbon, as described hereinabove, said body having been annealed in the presence of a magnetic field. The present invention further provides a method for producing the alloys comprising the step of supplying at least a portion of the boron content thereof from carbothermic ferroboron. The amoφhous metallic alloys of the invention have a high saturation induction, a high Curie temperature and a high crystallization temperature in combination with a low core loss and a low exciting power at line frequencies, obtained over a range of annealing conditions, as compared to the prior art alloys. Such a combination makes the alloys of the invention particularly suited for use in cores of transformers for an electrical power distribution network. Other uses may be found in special magnetic amplifiers, relay cores, ground fault interrupters, and the like. Brief Description of the Drawings The invention will be more fully understood, and farther advantages will become apparent, when reference is made to the following detailed description of the preferred embodiments of the invention and the accompanying drawings in which: Figures 1(a)- 1(g) are ternary cross-sections of the quaternary Fe-B-Si-C composition space at various values of iron, as noted, illustrating the basic and preferred alloys of this invention; Figures 2(a)-2(f) are ternary cross-sections of the quaternary Fe-B-Si-C composition space at various values of iron, as noted, providing the values for the crystallization temperatures, in °C, of the respective alloy compositions, which are as plotted, and wherein the corresponding ranges of the basic alloys of this invention are also shown; Figures 3(a)-3(f) are ternary cross-sections of the quaternary Fe-B-Si-C composition space at various values of iron, as noted, providing the values for the Curie temperatures, in °C, of the respective alloy compositions, which are as plotted, and wherein the corresponding ranges of the basic alloys of this invention are also shown; and Figures 4(a)-4(d) are ternary cross-sections of the quaternary Fe-B-Si-C composition space at various values of iron, as noted, providing the values for the saturation magnetic moment, in emu/g, of the respective alloy compositions, which are as plotted, and wherein the corresponding ranges of the basic alloys of this invention are also shown. Description of the Preferred Embodiments The present invention provides novel metallic alloys composed of iron, boron, silicon, and carbon, which are at least about 70% amoφhous, and which consist essentially of the composition Fe a B D Si c Cd, wherein "a" - "d" are in atomic percent, the sum of "a", "b", "c", and "d" equals 100, "a" ranges from about 77 to 80, "b" ranges from about 7 to 11.5, "c" ranges from about 3 to 12, and "d" ranges from about 2 to 6, with the proviso that when "c" is greater than 7.5 "d" is at least about 4, the alloy having up to about 0.5 atomic percent of impurities and a crystallization temperature of at least 500°C. For illustrative puφoses, the composition space defining a quaternary alloy may conveniently be depicted in graphical form using ternary cross-sections of the quaternary composition space of the constituents. That is, a psuedo-ternary diagram is used to represent the range of possible contents of three of the constituents at a fixed value of the fourth component. This representation is used in Figures l(a)-(g) to depict the Fe-B-Si-C alloy of the invention as regions in pseudo- ternary B-Si-C phase diagrams at various fixed contents of Fe. The composition of the alloy of the invention is such that: (i) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 80, "b", "c" and "d" are in the region A, B, C, D, E, F, G, A, illustrated in Figure 1(a); (ii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 79.5, "b", "c" and "d" are in the region A, B, C, D, E, F, A, illustrated in Figure 1(b); (iϋ) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 79, "b M , "c" and "d" are in the region A, B, C, D, E, A, illustrated in Figure 1(c); (iv) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 78.5, "b", "c" and "d" are in the region A, B, C, D, E, A, illustrated in Figure 1(d); (v) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 78, "b", "c" and "d" are in the region A, B, C, D, E, A, illustrated in Figure 1(e); (vi) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 77.5, "b", "c" and "d" are in the region A, B, C, D, E, A, illustrated in Figure 1(f); and, (vii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 77, "b", "c" and "d" are in the region A, B, C, D, A, illustrated in Figure 1(g). More specifically, referring to Figure 1, the compositions of the alloys defining the corners of the various polygons that depict the alloys of the invention as described above, are approximately as follows: (i) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 80 atomic percent Fe, the corners are defined by the alloys FesoBj i 5Si6 5C2, Fe8θBl l.5Si3C5.5, Fe8θBnSi3C6, FesoB7Si7C 6 , FesoB7Si9C4, Fe80B8.5Si7.5 4, Fe80B10.5Si7.5C2, and Fe80Bn.5Si6.5C2; (ii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 79.5 atomic percent Fe, the corners are defined by the alloys Fe79.5Bl ' 1.5Si7C2, Fe79.5Bn.5Si3C6, Fe79.5B7Si7.5C6, Fe79.5B7Si9.5C4, Fe79.5B9Si7.5C4, Fe79.5BnSi7 5C2 and Fe79 . 5Bn.5Si7C2; (iii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 79 atomic percent Fe, the corners are defined by the alloys Fe79Bl l.5Si7.5C2, Fe79Bn 5Si3 5C6, Fe79B7SisC6, Fe79B7SiιoC4, Fe79B9.5Si7.5C4, and Fe79Bn.5Si7.5C2; (iv) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 78.5 atomic percent Fe, the corners are defined by the alloys Fe78.5Bl l.5Si7.5C2.5, Fe g.sBi i .sSUCβ, Fe78.5B7Si8.5C6, Fe78.5B7Si10.5C4, Fe78.5BlθSi7.5C4, and Fe78.5Bn.5Si7.5 c 2.5; (v) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 78 atomic percent Fe, the corners are defined by the alloys Fe78Bn.5Si7.5C3, Fe78Bl l.5S14.5C6, Fe78B7Si 9 C6, Fe7 8 B7SinC4, Fe78BlO.5Si7.5C4, and Fe78Bn.5Si7.5C3; (vi) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 77.5 atomic percent Fe, the corners are defined by the alloys Fe77.5Bl l.5Si7.5C3.5, Fe77.5Bn 5Si5C6, Fe77.5B7Si9.5C6, Fe77.5B7Sin . 5C4, Fe77.5BnSi7.5C4, and Fe77.5Bπ 5Si7 . 5C j .5; and (vii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 77 atomic percent Fe, the corners are defined by the alloys Fe77Bn.5Si7.5C4, Fe77Bn.5Si5.5C6, Fe77B7SiιoC6, Fe77B7Sii2C4, and Fe77Bl l.5Si7.5C4. The alloys of this invention evidence the combination of a high crystallization temperature of at least 500°C, a high Curie temperature of at least about 360°C, a high saturation magnetization corresponding to a magnetic moment of at least about 165 emu/g and, a low core loss not greater than about 0.35 W/kg and a low exciting power value not greater than about 1 VA/kg, when measured at 25°C, 60 Hz and 1.4 T, after the alloys have been annealed at a temperature within the range of about 3-30°C-390°C, for a time ranging between about 0.5 and 4 hours, in the presence of a magnetic field in the range of about 5-30 Oe. As is well known, the magnetic properties of alloys cast to a metastable state generally improve with increased volume percent of amoφhous phase. Accordingly, the alloys of this invention are cast so as to be at least about 70% amoφhous, preferably at least about 90% amoφhous, and most preferably essentially 100% amoφhous. The volume percent of amoφhous phase in the alloy is conveniently determined by x-ray diffraction. The preferred alloys of the invention consist essentially of the composition Fe a BbSi c C(i, wherein "a" - "d" are in atomic percent, the sum of "a", "b", "c", and "d" equals 100, "a" ranges from about 78 to 80, and "b" ranges from about 8 to 11. It is believed that with a B content of at least 8 at.% such alloys are more readily cast to be at least 90%, and most preferably essentially 100% amoφhous. The limitation of B content to at most about 11% further reduces the raw material cost of the alloy. An Fe content of at least about 78% raises the saturation magnetization of the alloy. In these preferred alloys of the invention a combination of higher Curie temperatures (greater than about 380°C) and lower core losses (less than about 0.28 W/kg at 60 Hz and 1.4 T at 25°C) is obtained. The preferred alloys of the invention are depicted for illustrative puφoses in Figures l(a)-(e). The composition of the preferred alloy of the invention is such that: (i) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 80, "b", "c" and "d" are in the region P, C, Q, R, F, G, P, illustrated in Figure 1(a); (ii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 79.5, "b", "c" and "d" are in the region F, Q, R, S, E, F, illustrated in Figure 1(b); (iii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 79, "b", "c" and "d" are in the region P, Q, R, S, E, P, illustrated in Figure 1(c); (iv) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 78.5, "b", "c" and "d" are in the region P, Q, R, S, E, P, illustrated in Figure 1(d); and (v) " in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 78, "b", "c" and "d" are in the region P, Q, R, S, E, P, illustrated in Figure 1(e). More specifically, referring to Figures l(a)-(e), the compositions of the alloys defining the co ers of the various polygons that depict the preferred alloys of the invention as described above, are approximately as follows: (i) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 80 atomic percent Fe, the comers are defined by the alloys FesoB 11 Si7C2, Fe8θBnSi3C6, FesoBsSiόCό, FesoBsSisC^ Fe80B8.5Si7.5 4, Fe80BlO.5Si7.5 2, and Fe8θBl lSi7C2; (ii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 79.5 atomic percent Fe, the comers are defined by the alloys Fe79.5BnSi7.5C2, Fe79.5BnSi3.5C6, Fe79.5B8Si6.5C6, Fe79.5B8Si8.5C4, Fe79.5B9Si7.5C4, and Fe79.5BuSi7 5C2; (iii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 79 atomic percent Fe, the comers are defined by the alloys Fe7 9 BnSi7.5C2.5, Fe79BnSi4C 6 , Fe79BsSi7C6, Fe79B 8 Si9C 4 , Fe79B9.5Si7.5C4, and Fe79BnSi7.5C2.5; (iv) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 78.5 atomic percent Fe, the co ers are defined by the alloys Fe78.5BllSi7.5C3, Fe7g.5Bl iSi4.5C6, Fe78.5B8Si7.5C6, Fe78.5BsSi9 . 5C4, Fe78.5Bi0Si7.5C4, and Fe78.5BnSi7.5C3; (v) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 78 atomic percent Fe, the comers are defined by the alloys Fe 7 8BnSi7.5C3.5, Fe 78 Bι ιSi5C6, Fe 7 8B8Si8C 6 , Fe78B8SiioC , Fe78B10.5Si7.5C4, and Fe78Bι 1Si7.5C3.5- The more preferred alloys of this invention consist essentially of the composition Fe a B D Si c Cd, where "a" - "d" are in atomic percent, the sum of "a", "b", "c", and "d" equals 100, "a" ranges from about 79 to 80, "b" ranges from about 8.5 to 10.5, and "d" ranges from about 3 and 4.5. These more preferred alloys of the invention exhibit, in combination, Curie temperatures higher than about 390°C, crystallization temperatures often higher than about 505°C, saturation magnetization values corresponding to a magnetic moment of at least about 170 emu/g, and often to magnetic moments of about 174 emu/g, and particularly low core losses, typically lower than about 0.25 W/kg at 60 Hz and 1.4 T at 25°C, and often lower than about 0.2 W/kg under the same test conditions. These properties are obtained even with a maximum B content of about 10.5 in the more preferred alloy which further lowers its raw material cost. Carbon content in the more preferred alloy is restricted, balancing improvement in castability and thermal stability with reduction of raw materials cost. Fe content of at least about 79% assures adequate saturation magnetization. Examples of the more preferred alloys of the invention include Fe79.5B9.25Si7.5C3.75, Fe79B8.5Si8.5C4, Fe79. ιBg.9Si8C4, and Fe79 7 B 9 Si 7 2C4 0- The more preferred alloys of the invention are depicted for illustrative puφoses in Figures l(a)-(c). The composition of the preferred alloy of the invention is such that: (i) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 80, "b", "c" and "d" are in the region 1, 2, 3, F, 4, 1, illustrated in Figure 1(a); (ii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 79.5, "b", "c" and "d" are in the region 1, 2, 3, 4, E, 5, 1, illustrated in Figure 1(b); and (iii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at "a" = 79, "b", "c" and "d" are in the region 1, 2, 3, 4, E, 1, illustrated in Figure 1(c). More specifically, referring to Figures l(a)-(c), the compositions of the alloys defining the comers of the various polygons that depict the more preferred alloys of the invention as described above, are approximately as follows: (i) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 80 atomic percent Fe, the comers are defined by the alloys FesoB10.5Si6.5C3, Fe8θBlθ.5Si5C4.5, FesoB8.5Si7C4.5, FesoB8.5Si7.5C4, FesoB9.5Si7.5C3, and e8OBlO.5Si6.5C3; (ii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 79.5 atomic percent Fe, the co ers are defined by the alloys Fe79.5Bl0.5Si7C3, Fe79.5Bιo.5Si5.5 -4.5, Fe79.5Bs.5Si7.5 4.5, Fe79.5B8.5Si8C4, Fe79.5B9Si7.5C4, Fe79.5B10Si7.5C3, and Fe79.5Bιo.5SΪ7C3, and (iii) in the ternary cross-section of the quaternary Fe-B-Si-C composition space at 79 atomic percent Fe, the comers are defined by the alloys Fe79Bio.5Si7.5C3, Fe79Bιo.5Si6C4.5, Fe79B8.5SisC4.5, Fe79Bs.5Si8.5C4, Fe79B9.5S17 5C4, and Fe79B10.5Si7.5C3. A still more preferred alloy of the invention has a silicon content "c" of at least about 6.5 further to enhance thermal stability and formability. The purity of the alloys of the present invention is, of course, dependent upon the purity of the materials employed to produce the alloys. Raw materials which are less expensive and, therefore contain a greater impurity content, could be desirable to ensure large scale production economics, for example. Accordingly, the alloys of this invention can contain as much as about 0.5 atomic percent of impurities, but preferably contain not more than 0.3 atomic percent of impurities. Here, all elements apart from Fe, B, Si, and C are considered as impurities. The impurity content would, of course, modify the actual levels of the primary constituents in the alloys of the invention from their intended values. However, it is anticipated that the ratios of the proportions of Fe, B, Si, and C will be maintained. Metallic alloy chemistry can be determined by various means known in the art including inductively coupled plasma emission spectroscopy (ICP), atomic absoφtion spectroscopy (AAS), and classical wet chemistry (gravimetric) analysis. Because of its simultaneous analysis capability, ICP is a method of choice in industrial laboratories. An expeditious mode for operating an ICP system is the "concentration ratio" mode, in which a series of selected major and impurity elements is simultaneously analyzed directly and the major constituent is calculated by the difference between 100 percent and the elements analyzed. Thus, impurity elements for which there is no direct measurement in the ICP system are reported as part of the calculated major element content. That is, the true content of major element in a metallic alloy analyzed by ICP in the concentration ratio mode is actually slightly less than that calculated due to the presence of very low levels of impurities which are not directly measured. The alloy chemistries of the present invention pertain to the relative amounts of Fe, B, Si, and C, normalized to 100 percent. Impurity element contents are not considered to be comprised in the sum of major elements adding up to 100 percent. For casting of the metallic glass alloy of the invention in tonnage quantities on a commercial scale, it is imperative that the production method be as reliable as possible and incoφorate the cheapest possible raw materials. The most expensive constituent of the alloy is boron. Although the alloy melt may be prepared from boron in its elemental form, the use of ferroboron is highly preferred., both for the lower effective cost per unit weight of boron and for the greater reliability and repeatability it affords to the process. In contrast to ferroboron which is easily melted and incoφorated into the present alloy, elemental boron has a low enough mass density that it floats to the surface when added to a large melt. It is thus difficult to assure reproducibly that elemental boron is fully incoφorated without any being left unmelted or entrained in the surface slag layer. Ferroboron is produced commercially by either aluminothermic or carbothermic reduction processes. These processes are conventional in the art and are described in detail in an article, "Production of Ferroalloys", ed. J.H. Dowling, Electric Furnace Proceedings, vol. 41, Detroit, MI, 6-9 Dec. 1983 (Iron and Steel Society/ AIME Warrendale, PA, 1984), the teaching of which is incoφorated herein by reference thereto. Carbothermic ferroboron is preferred for the alloy of the invention. When incoφorated in amoφhous Fe-base alloys, aluminothermic ferroboron may introduce impurity levels of aluminum which are somewhat deleterious both to the casting process itself and to the ultimate magnetic properties of the alloy. Hence, it is preferred that the alloy of the invention be produced by a process in which at least 80% of the boron is supplied from carbothermic ferroboron. More preferably substantially all of the boron is supplied from carbothermic ferroboron. Commercial grades of carbothermic ferroboron have carbon contents typically varying from about 0.15 to as much as 0.5 wt.%, with boron content of about 15-20 wt.%. Because the alloy of the invention contains appreciable carbon, a greater content of carbon impurity in the ferroboron may be accepted than for ferroboron used in substantially carbon-free alloys. By tolerating this higher impurity content, the producer of the alloy of this invention may use a markedly less expensive grade of ferroboron, thereby advantageously reducing the overall raw material cost of the alloy. Similarly, the producer of the alloy of this invention may tolerate less expensive sources of Fe metal which also have higher carbon content. The compositions of various Fe-B-Si-C alloys that were actually cast are shown in Figures 2(a)-2(f) or 3(a)-3(f). All of the alloys recited here were cast as 6 mm wide ribbons, in 50-100 g batches, in accordance with the following procedure: The alloys were cast on a hollow, rotating cylinder, open at one side thereof. The cylinder had an outer diameter of 25.4 cm and a casting surface having a thickness of 0.25" (0.635 cm) and a width of 2" (5.08 cm). The cylinder was made from a Cu-Be alloy produced by Brush- Wellman (designated Brush- Wellman Alloy 10). The constituent elements of the alloys tested were mixed in appropriate proportions, starting from high purity (B=99.9%, and Fe and Si at least 99.99% pure) raw materials, and melted in a 2.54 cm diameter quartz crucible to yield homogenized, pre-alloyed ingots. These ingots were loaded into a second quartz crucible (2.54 cm diameter), with the bottom ground flat and containing a rectangular slot of dimensions 0.25" x 0.02" (0.635 cm x .051 cm), positioned 0.008" (*0.02 cm) from the casting surface of the cylinder. The cylinder was rotated at a peripheral speed of about 9,000 feet per minute (45.72 m/s). The second crucible and wheel were enclosed within a chamber pumped down to a vacuum of about 10 mm Hg. The top of the crucible was capped and a slight vacuum was maintained in the crucible (a pressure of about 10 mm Hg). A power supply (Pillar Coφoration lOkW), operating at about 70% of peak power, was used to induction melt each of the ingots. When the ingot was fully molten, the vacuum in the crucible was released, enabling the melt to contact the wheel surface and be subsequently quenched into ribbons about 6 mm wide via the principle of planar flow casting disclosed in USP 4,142,571, which is incoφorated herein by reference thereto. Some of the alloy compositions belonging to the invention, as well as some alloy compositions outside the scope of the invention, were also cast as ribbons ranging in width between about 1" and 6.7" on larger casting machines, in batches ranging from about 5-1000 kg. The principle of planar flow casting was still used. The sizes of the crucibles and pre-alloyed ingots, and various casting parameters, were, of necessity, different from those described above. Furthermore, due to the higher heat loads, different casting substrate materials were also employed. In many instances in the case of the larger casting runs, the intermediate step of the pre-alloyed ingot was dispensed with, and/or raw materials of commercial purity were employed. In instances when commercial, high grade raw materials were used, chemical analysis on the cast ribbons revealed that the impurity content ranged between about 0.2 and 0.4 percent by weight. Some of the trace elements detected, such as Ti, V, Cr, Mn, Co, Ni, and Cu, have atomic weights comparable to that of Fe, while other detected elements, such as Na, Mg, Al, and P, are comparable to Si in atomic weight. The heavy elements detected were Zr, Ce, and W. Given this distribution, it is estimated that the detected total of 0.2 to 0.4 weight percent corresponds to a range of about 0.25 to 0.5 atomic percent for the impurity content. It was generally found that when the B and/or the Si contents were lower, and/or the C content higher, than the respective limits specified for the alloys of this invention, the resulting alloys were unacceptable for a variety of reasons. In many instances, these alloys were brittle and difficult to handle, even in the as-cast state. In other instances, it was found that the melt was difficult to homogenize, with the result that the control of the composition in the cast ribbon was difficult. Even though, with great care and effort, some of these chemistries could be made into ductile ribbons with the correct composition, such alloy compositions would surely not be amenable to large scale continuous production of acceptable ribbons, and, therefore, these alloys are undesirable. As discussed previously, because of the very high cost of boron as a raw material, higher boron levels than prescribed here for the alloys of the invention are economically unattractive, and, therefore, not desired. The Figures 2 also contain the measured values of the crystallization temperatures, and the Figures 3 provide the measured values of the Curie temperatures of these alloys. In each of these figures, the delimiting polygons for the basic alloys of this invention are also shown for reference. The crystallization temperature of these alloys was determined by Differential Scanning Calorimetry. A scanning rate of 20 K/min was used, and the crystallization temperature was defined as the temperature of onset of the crystallization reaction. The Curie temperature was determined using an inductance technique. Multiple helical turns of high temperature, ceramic-insulated copper wire, identical in all respects (length, number and pitch), were wound onto two open-ended quartz tubes. The two sets of windings thus prepared had the same inductance. The two quartz tubes were placed in a tube furnace, and an AC exciting signal (with a fixed frequency ranging between about 2 kHz and 10 kHz) was applied to the prepared inductors, and the balance (or difference) signal from the inductors was monitored. A ribbon sample of the alloys to be measured was inserted into one of the tubes, serving as the "core" material for that inductor. The high permeability of the ferromagnetic core material caused an imbalance in the values of the inductances and, therefore, a large signal. A thermocouple attached to the alloy ribbon served as the temperature monitor. When the two inductors were heated up in an oven, the imbalance signal essentially dropped to zero when the ferromagnetic metallic glass passed through its Curie temperature and became a paramagnet (low permeability). The two inductors then yielded about the same output. The transition region is usually broad, reflecting the fact that the stresses in the as-cast glassy alloy are relaxing. The midpoint of the transition region was defined as the Curie temperature. In the same fashion, when the oven was allowed to cool, the paramagnetic-to- ferromagnetic transition could be detected. This transition, from the at least partially relaxed glassy alloy, was usually much shaφer. The paramagnetic-to-ferromagnetic transition temperature was higher than the ferromagnetic-to-paramagnetic transition temperature for a given sample. The quoted values in the Figures 3 for the Curie temperatures represent the paramagnetic-to-ferromagnetic transition. The importance of high crystallization and Curie temperatures has to do with the efficient accomplishment of necessary anneals on the as-cast amoφhous metallic alloy strips. In the production of magnetic cores from amoφhous metallic alloy strip (metallic glass) for use in distribution and power transformers, the metallic glass, either before or after being wound into a core, is subjected to annealing. Annealing (or, synonymously, heat treatment), usually in the presence of an applied magnetic field, is necessary before the metallic glass will display its excellent soft magnetic characteristics, because as-cast metallic glasses exhibit a high degree of quenched-in stress which causes significant stress-induced magnetic anisotropy. This anisotropy masks the true soft magnetic properties of the product and is removed by annealing the product at suitably chosen temperatures at which the induced quenched-in stresses are relieved. Obviously, the annealing temperature must be below the crystallization temperature. Since annealing is a dynamic process, the higher the annealing temperature, the shorter the time period needed to anneal the product. For these and other reasons to be explained below, the optimum annealing temperature is presently in the narrow range of from about 140 K to 100 K below the crystallization temperature of the metallic glass, and the optimum annealing time is about 1.5-2.5 hours; for large cores, that is, cores having mass in excess of 50 kg, somewhat longer times ranging up to about 4 hours may be required. Metallic glasses exhibit no magnetocrystalline anisotropy, a fact attributable to their amoφhous nature. However, in the production of magnetic cores, especially those for Use in distribution transformers, it is highly desirable to maximize the magnetic anisotropy of the alloy along a preferred axis aligned with the length of the strip. In fact, presently, it is believed to be the preferred practice of transformer core manufacturers to apply a magnetic field to the metallic glass during the annealing step in order to induce a preferred axis of magnetization. The field strength ordinarily applied during annealing is sufficient to saturate the material in order to maximize the induced anisotropy. Considering that the saturation magnetization value decreases with increasing temperature until the Curie temperature is reached, above which temperature no further modification of magnetic anisotropy is possible, annealing is preferably carried out at temperatures close to the Curie temperature of the metallic glass so as to maximize the effect of the external magnetic field. Of course, the lower the annealing temperature, the longer the time (and higher the applied magnetic field strength) necessary to relieve the cast-in stresses and to induce a preferred anisotropy axis. It should be apparent from the above discussion that selection of the annealing temperature and time depends in large part on the crystallization temperature and Curie temperature of the material. In general, the higher these temperatures are, the higher the anneal temperatures could be and, therefore, the anneal process cculd be accomplished in a shorter time. It is noted from the Figures 2 and 3 that the crystallization and Curie temperatures generally increase with decreasing iron content. In addition, for a given iron content, the crystallization temperature generally decreases with a decrease in the boron content. Iron contents higher than about 81 atomic percent are not desirable; both the crystallization and the Curie temperatures would be adversely affected. This increase is approximately in the range of 20°-25°C in the crystallization temperature, and approximately in the range of 10°-15°C in the Curie temperature, per atomic percent decrease in iron content. Such a smooth dependence of these temperatures on the iron content is a distinguishing, and desirable, characteristic of the alloys of this invention. For example, during the course of large scale production of these materials, the reasonably rapid measurement of the crystallization temperature could be used as a quality control tool on the composition of the cast ribbon. Actual evaluation of the chemistries is a more time consuming process. In addition, the characteristic of a smooth dependence of material properties on the composition is preferable for the commercial scale production of materials, where, of necessity, the alloy composition cannot be controlled to specifications as tight as in a laboratory. A crystallization temperature of at least 500°C is preferred in an amoφhous alloy useful as magnetic core material in a transformer to ensure that, during annealing or in use in a transformer (particularly in the event of a current overload), the risk of inducing crystallization into the alloy is minimized. As stated previously, the Curie temperature of an amoφhous alloy should be close to, and preferably slightly higher than, the temperature employed during annealing. The closer the annealing temperature is to the Curie temperature, the easier it is to align the magnetic domains in a preferred axis, thus minimizing the losses exhibited by the alloys when magnetized along that same axis. A useful transformer core alloy should have a Curie temperature of at least about 360°C; lower values would result in lower anneal temperatures and long anneal times. However, very high Curie temperatures are also not very desirable. Anneal temperatures should not be too high for various reasons: at high anneal temperatures, control of anneal time becomes critical, because even a partial crystallization of the alloy has to be avoided, and, even if crystallization does not pose a potential problem, control of anneal time remains critical, so that the risk of substantial loss of ductility, and subsequent handleability, is minimized; additionally, as will be described later, anneal temperatures have to be "realistic", and not too high, in terms of ovens conventionally used to anneal large cores, and the necessary management of the attendant temperature gradients, to ensure useful and "optimal" cores. On the other hand, if the anneal temperatures are not increased when a high Curie temperature material is annealed, impractically large external fields will be required to ensure a favorable alignment of the magnetic domains. While there may be other individual compositions, with higher silicon content than in the alloys of this invention, that have values for their crystallization and/or Curie temperatures which are comparable to those of the alloys of this invention, the dependence of these values on the alloy composition is more complex, and not as systematic as observed in the alloys of this invention. As may be noted from the Figures 2 and 3, when one ventures outside of the Si contents specified for the alloys of this invention, the crystallization or the Curie temperature tends to be generally sensitive to alloy composition; either the crystallization temperature drops or the Curie temperature increases. As discussed above, since the crystallization and Curie temperatures of an amoφhous material help to define the anneal condition for the material, and since, in practice, these anneal conditions are strictly adhered to during the production of large transformer cores, alloy compositions wherein the material properties are not generally forgiving in terms of small variations in composition are not desirable. It has been found that the saturation magnetic moment is a slowly varying function of the iron content in these alloys, decreasing in value as the iron content is decreased. This is illustrated by example in Figures 4(a)-4(d). The values for the saturation magnetization quoted are those obtained from as-cast ribbons. It is well understood in the art that the saturation magnetization of an annealed metallic glass alloy is usually higher than that of the same alloy in the as- cast state, for the same reason as discussed previously: the glass is relaxed in the annealed state. A commercial vibrating sample magnetometer was used for the measurement of the saturation magnetic moment of these alloys. As-cast ribbon from a given alloy was cut into several small squares (approximately 2 mm x 2 mm), which were randomly oriented about a direction normal to their plane, their plane being parallel to maximum applied field of about 9.5 kOe. By using the measured mass density, the saturation induction, B s , may then be calculated. Not all of the cast alloys were characterized for saturation magnetic moment. The density of many of these alloys was measured using standard techniques based upon Archimedes' Principle. It is apparent from the Figures 4 that iron contents below about 77 atomic percent are not desirable, since the saturation magnetic moments fall to unacceptably low levels. Since electrical distribution transformers are usually designed to operate at 90% of the available saturation induction at 85°C, and since a higher design induction generally leads to more compact magnetic cores, a high saturation moment, and, therefore, high saturation induction, in combination with a high Curie temperature is important from a transformer core designer's point of view. The saturation magnetic moment in an alloy useful as transformer core material should be at least about 165 emu/g, and preferably about 170 emu/g. Since Fe-B-Si-C alloys generally have a greater mass density than Fe-B-Si alloys, the above numbers would be consistent with established criteria for Fe-B-Si alloys for use as transformer core materials. It is noted from the Figures 4 that some of the most preferred alloys of the invention have these moments to be as high as 175 emu/g. In addition to factors such as crystallization and Curie temperatures, an important consideration in selecting annealing temperature and time is the effect of the anneal on the ductility of the product. In the manufacture of magnetic cores for distribution and power transformers, the metallic glass must be sufficiently ductile so as to be wound or assembled into the core shape and to enable it to be handled after having been annealed, especially during subsequent transformer manufacturing steps such as the step of lacing the annealed metallic glass through the transformer coϋ. (For a detailed discussion of the process of manufacturing transformer core and coil assemblies see, for example, USP 4,734,975). Annealing of an iron-rich metallic glass results in degradation of the ductility of the alloy. While the mechanism responsible for degradation prior to crystallization is not clear, it is generally believed to be associated with the dissipation of the "free volume" quenched into the as-cast metallic glass. The "free volume" in a glassy atomic structure is analogous to vacancies in a crystalline atomic structure. When a metallic glass is annealed, this "free volume" is dissipated as the amoφhous structure tends to relax into a lower energy state represented by a more efficient atomic "packing" in the amoφhous state. Without wishing to be bound by any theory, it is believed that since the packing of Fe-base alloys in the amoφhous state more closely resembles that of a face centered cubic structure (a close-packed crystalline structure) rather than the body centered cubic structure of iron, the more relaxed the iron-base metallic glass, the more brittle it is (i.e., less able it is to tolerate external strain). Therefore, as the annealing temperature and/or time increase, the ductility of the metallic glass decreases. Consequently, apart from the fundamental issue of alloy composition, one must consider the effects of annealing temperature and time to further ensure that the product retains sufficient ductility to be used in the production of transformer cores. The two most important characteristics of the performance of a transformer core are the core loss and exciting power of the core material. When magnetic cores of annealed metallic glass are energized (i.e., magnetized by the application of a magnetic field) a certain amount of the input energy is consumed by the core and is lost irrevocably as heat. This energy consumption is caused primarily by the energy required to align all the magnetic domains in the metallic glass in the direction of the field. This lost energy is referred to as core loss, and is represented quantitatively as the area circumscribed by the B-H loop generated during one complete magnetization cycle of the material. The core loss is ordinarily reported in units of W/kg, which actually represents the energy lost in one second by a kilogram of material under the reported conditions of frequency, core induction level and temperature. Core loss is affected by the annealing history of the metallic glass. Put simply, core loss depends upon whether the glass is under-annealed, optimally annealed or over-annealed. Under-annealed glasses have residual, quenched-in stresses and related magnetic anisotropies which require additional energy during magnetization of the product and result in increased core losses during magnetic cycling. Over- annealed alloys are believed to exhibit maximum "packing" and/or can contain crystalline phases, the result of which is a loss of ductility and/or inferior magnetic properties such as increased core loss caused by increased resistance to movement of the magnetic domains. Optimally annealed alloys exhibit a fine balance between ductility and magnetic properties. Presently, transformer manufacturers utilize amoφhous alloy exhibiting core loss values of less than .37 W/kg (60 Hz and 1.4 T at 25°C). Exciting power (also termed apparent power) is the electrical energy required to produce a magnetic field of sufficient strength to achieve in the metallic glass a given level of magnetization. An as-cast iron-rich amoφhous metallic alloy exhibits a B-H loop which is somewhat sheared over. During annealing, as-cast anisotropies and cast-in stresses are relieved, the B-H loop becomes more square and narrower relative to the as-cast loop shape until it is optimally annealed. Upon over- annealing, the B-H loop tends to broaden as a result of reduced tolerance to strain and, depending upon the degree of over-anneahng, existence of crystalUne phases Thus, as the annealing process for a given alloy progresses from under-annealed to optimally annealed to over-annealed, the value of H for a given level of magnetization initially decreases, then reaches an optimum (lowest) value, and thereafter increases. Therefore, the electrical energy necessary to achieve a given magnetization (the exciting power) is minimized for an optimally-annealed alloy. Presently, transformer core manufacturers employ amoφhous alloy exhibiting exciting power values at 60 Hz and 1.4 T (at 25°C) of about 1 VA/kg or less. It should be apparent that optimum annealing conditions are different for amoφhous alloys of different compositions, and for each property required. Consequently, an "optimum" anneal is generally recognized as that anneaUng process which produces the best balance between the combination of mechanical and electrical characteristics necessary for a given appUcation. In the case of transformer core manufacture, the manufacturer determines a specific temperature and time for annealing which are "optimum" for the aUoy employed and does not deviate from that temperature or time. In practice, however, anneaUng furnaces and furnace control equipment are not precise enough to maintain exactly the optimum anneaUng conditions selected. In addition, because of the size of the cores (typicaUy up to 200 kg each) and the configuration of furnaces, cores may not heat uniformly, thus producing over- annealed and under-annealed core portions. Therefore, it is of utmost importance not only to provide an aUoy which exhibits the best combination of properties under optimum conditions, but also to provide an aUoy which exhibits that "best combination" over a range of anneaUng conditions. The range of anneaUng conditions under which a useful product can be produced is referred to as an " annealing (or anneal) window" . As stated earUer, the optimum anneaUng temperature and time for metalhc glass presently used in transformer manufacture is a temperature in the range of 140° -100°C below the crystallization temperature of the aUoy, for a time of between 1.5- 2.5 hours. The aUoys of the present invention offer an anneaUng window of about 20-25° C for the same optimum anneal time. Thus, alloys of the present invention can be subjected to anneaUng temperature variations of about ±10°C from the optimum anneaUng temperature and still retain the combination of characteristics essential to the economical production of transformer cores. Moreover, the aUoys of the present invention show unexpectedly enhanced stabihty in each of the characteristics of the combination over the range of the anneal window; a characteristic which enables the transformer manufacturer to more reliably produce uniformly performing cores. It has been disclosed that the frequency dependence of the core loss L of soft magnetic cores under sinusoidal excitation at frequency f may be represented by the following equation: L = af + bf" + cf 2 . The term af is the dc hysteresis loss (the limiting value of loss as frequency approaches zero), the term cf 2 is the classical eddy current loss, and the term br 11 represents the anomalous eddy current loss (see, e. g., G. E. Fish et al., J. Appl. Phys. 64, 5370 (1988)). Amoφhous metals generally possess sufficiently high resistivity " and low thickness that the classical eddy current losses may be neglected. Further, it has been disclosed that the exponent n for amoφhous metals is often about 1.5. Without being bound by any theory, it is beUeved that this value of n is indicative that the number of domain waUs active in the magnetization process varies with frequency. If the n= 1.5 value is representative, the hysteresis coefficient a and the eddy current coefficient b may be extracted conveniently by plotting as a straight line the core loss per cycle L/f versus the square root off. The f=0 intercept of the line is then a and the slope is b. Quite unexpectedly, the inventors have found that cores comprised of prior art aUoy and of aUoy of the invention may exhibit quite a different balance between the hysteresis and eddy current components of loss. Therefore, cores of different material which have similar losses at one frequency may have quite different losses at another frequency. In particular, cores of the present invention show at line frequency a smaUer value of eddy current loss but a higher value of hysteresis loss than similar cores of prior art amoφhous metal. Therefore, total core losses of the present aUoy which are only sUghtly lower at line frequency than those of prior art Fe-base aUoy would be substantially lower at higher frequency. Such a difference makes the aUoy and cores of the present invention especiaUy advantageous for use in airborne electrical equipment operating at 400 Hz and in other electronic applications in the kilohertz range. The alloy of the present invention is also advantageously employed in the construction of magnetic cores for filter inductors. It is weU known in the art that a filter inductor may be employed in electronic circuitry to impede selectively passage of alternating current noise or ripple superimposed on a desired dc current. For such appUcations, the filter inductor core frequently comprises at least one gap in the magnetic circuit thereof. By suitable choice of the gap the hysteresis loop of the core may be sheared to increase within controUed bounds the magnetic field required to saturate the core. Otherwise, the dc current component passing through the inductor would drive its core to saturation, reducing the effective permeabiUty seen by the ac current component and eliminating the desired filtering action. Although the flux excursion in the inductor core due to the ac current component passing through the winding thereof may be smaU, a large value of saturation magnetization is still important so a large dc current may pass without saturating the sheared B-H loop. As described in more detaϋ above, the aUoy of the invention preferably exhibits saturation magnetization of at least about 165 emu/g, and, more preferably, at least about 170 emu/g. Common means in the art for fabricating gapped cores include both radiaUy cutting in one or more places a generaUy toroidaUy shaped core and assembling punched or stamped C-I or E-I laminations. The foUowing examples are presented to provide a more complete understanding of the invention. The specific techniques, conditions, materials, proportions and reported data set forth to iUustrate the principles and practice of the invention are exemplary and should not be construed as limiting the scope of the invention. Example 1 Core loss and exciting power data were gathered from some representative aUoy samples of the invention prepared as follows: Toroidal samples for annealing, and subsequent magnetic measurements, were prepared by winding as-cast ribbons onto ceramic bobbins so that the mean path length of the ribbon core was about 126 mm. Insulated primary and secondary windings, each numbering 100, were applied to the toroids for the puφose of measurements of core loss. Toroidal samples so prepared contained between 3 and 20 g of ribbon in the case of 6 mm wide ribbons, and between 30 and 70 g for the wider ribbons. Annealing of these toroidal samples was carried out at 330°-390°C for 1-2.5 hours in the presence of an applied field of about 5-30 Oe imposed along the length of the ribbon (toroid circumference). This field was maintained while the samples were cooled following the anneal. The anneals were conducted under vacuum. The total core loss and exciting power were measured on these closed- magnetic-path samples under sinusoidal flux conditions using standard techniques The frequency (f) of excitation was 60 Hz, and the maximum induction level (Bm) that the cores were driven to was 1.4 T. The core losses and exciting powers obtained, at 60 Hz and 1.4 T at 25 °C, from annealed cores of representative alloys of this invention, and of some alloys not within the scope of this invention, are provided in Tables II and in for ribbons annealed for 1 hour at various temperatures, and in Table IV for ribbons annealed for 2 hours at various temperatures. The designations of the aUoys in these Tables refer to the corresponding compositions provided in Table I. As is noted from that Table, the aUoys designated as A-F are outside the scope of this invention. Not all of the aUoys were annealed under all sets of conditions quoted in the Tables. It is noted from these Tables that, for most of the alloys of this invention, the core losses are lesser than about 0.3 W/kg. Such is not the case with the aUoys not belonging to this invention. As mentioned previously, the core loss value presently specified by transformer manufacturers for their core material is about 0.37 W/kg. The exciting power values are also noted to be less than about 1 VA/kg, the value presently specified for transformer core materials. It is this combination of exciting power and core losses, in further combination with the other characteristics discussed previously, and the relative uniformity and consistency of the properties under a range of anneal conditions, which is a characteristic of, but unexpected from, alloys of the present invention. The anneal windows over which the advantageous combination of core performance characteristics is obtained are evident from the Tables II, III, and IV. It is particularly noted that, in the preferred range of chemistries for the aUoys of this invention, the core losses can be as low as about 0.2-0.3 W/kg, and the exciting powers can be as low as about 0.25-0.5 VA/kg. TABLE I Compositions of aUoys (in atomic percent) characterized for core loss and exciting power values. AUoys A-F are outside the scope of this invention. AUoys 1- 9 were cast as 6 mm wide ribbons. TABLE π Cores loss and exciting power values, measured at 60 Hz, 1.4 T, and 25°C, obtained from Fe-B-Si-C alloys following anneals for 1 hour at the various noted temperatures. The alloy designations are from Table I. TABLE UI Cores loss and exciting power values, measured at 60 Hz, 1.4 T, and 25°C, obtained from Fe-B-Si-C alloys following anneals for 1 hour at the various noted temperatures. The aUoy designations are from Table I. TABLE IV Cores loss and exciting power values, measured at 60 Hz, 1.4 T. 25°C, obtained from Fe-B-Si-C aUoys following anneals for 2 hours at the various noted temperatures. The alloy designations are from Table I. Example 2 In addition to the cores described above, ten larger toroidal cores were also constructed from some of the preferred aUoys of the invention, annealed, and tested. These cores had about 12 kg of core material. The ribbons chosen for these cores were 4.2" wide, and were derived from different large scale casts of two nominal alloy compositions: Fe79 5B925Si7 5C3 75 and Fe79B8.5Si8.5C4. The cores had an internal diameter of about 7" and an external diameter of about 9", and were annealed in an inert atmosphere nominally at 370°C for 2 hours. Due to the size of the cores, not aU of the core material may have been exposed to the anneal temperature for the same time. The resultant average core losses from these cores was 0.25 W/kg with a standard deviation of 0.023 W kg, and the average exciting power was 0.40 VA/kg with a standard deviation of 0.12 VA/kg, when measured under 60 Hz and 1.4 T at 25°C, for both the compositions studied. These values are comparable to those found in the smaller diameter cores for similar compositions. It is well understood in the art that, because of strains on the core material associated with winding of toroidal cores, the core losses measured on such cores are generally higher than those obtained if the material were to be annealed and characterized for core losses as an unstrained straight strip. In the case of ribbons wider than about 1", for example, for a given core bobbin diameter, this effect is more pronounced in the case of 30 to 70 g cores containing multiple windings of strips of core materials, than in the case of cores containing only a single layer or, at most, 2-3 layers of such ribbons. The measured core loss in a 30-70 g core often can be substantiaUy greater than that measured on a straight strip. This is one manifestation of what is referred to as the "destruction factor" in the transformer core manufacturing industry. The so caUed destruction factor (sometimes referred to as the "build factor") is usually defined as the ratio of the actual core loss obtained from the core material in a fully assembled transformer core and the core loss obtained from straight strips of the same material in a quality control laboratory. It is beUeved that the above referred effect of strains associated with winding the core material is not as great in the case of a "real life" transformer core, since the diameters are much larger in these cores, than in the laboratory cores described previously. The "destruction" in these cores is more a consequence of the core assembly procedure itself. As an example, in one scheme for transformer construction, the annealed core has to be opened up to aUow coils to be inserted around the core. Apart from the destruction associated with cutting, etc. of the core material, newly introduced stresses contribute to an increase in the core loss. Depending on the core construction scheme, a core loss value in the range of 0.2-0 3 W/kg in a small diameter toroidal core, as in the case of the exemplary cores of alloys of this invention, could conceivably increase to faU in the range of about 0.3-0.4 W kg in a "real" transformer core. Example 3 Wound test cores 11-16 of the metaUic glass alloy of the invention (nominal composition Fβ7 7B9 Si 2C4 Q ) were fabricated and annealed in an inert atmosphere using conventional methods. Each core comprised about 100 kg of ribbon 6.7" wide wound generaUy toroidaUy. These cores were of the approximate size appointed for use in commercial distribution transformers of 20-30 kVA rating. The requisite ribbons were cut and the core assembled by wrapping the first layer around a central mandrel and then wrapping each succeeding layer in turn around the preceding layer. Each layer was cut with a length such that its opposite ends overlapped slightly. After the final layer was added, steel bands were used to constrain the core during subsequent handling and anneaUng. The cuts aUow the core to be opened after anneaUng to allow sUding on copper windings and then to be relaced and secured, using methods commonly employed in the commercial construction of distribution transformer core-coU assemblies. The presence of gaps within each layer of core material is known to increase the exciting power of the core compared to the exciting power that would be exhibited by a core of the same geometry but without the gaps. The cores of this Example (Usted in Table V) were then annealed in the presence of a magnetic field appUed along the toroidal direction. Temperatures were measured by thermocouples. Each core was heated so that its center reached the temperature Usted and remained thereat for about 1 hour, then the cores were cooled to ambient in about 6 hours. The core losses and exciting powers under sinusoidal flux excitation at 60 Hz were determined using standard methods including an average responding voltmeter to measure flux, RMS-responding meters to measure current, voltage, and exciting power, and an electronic wattmeter to measure power loss. Core loss and exciting power data for these cores measured at room temperature at maximum inductions of 1.3 T and 1.4 T are depicted in Table V below. TABLE V Core Annealing Center 1.4 T 1.3 T Number Field Temperature Loss VA Loss VA (Oe) (°C) (W/kg) (VA/kg) (W/kg) (VA/kg) 11 6 340 0.282 0.824 0.23 0.465 12 6 325 0.301 2.13 0.251 0.984 13 6 340 0.284 0.971 0.218 0.379 14 12 340 0.267 0.873 0.222 0.522 15 12 337 0.256 1.12 0.212 0.572 16 12 330 0.266 1.79 ~ — It is to be noted that even with the gaps described above, the cores in this Example exhibited a combination of low core loss and low exciting power when measured at room temperature under 60 Hz sinusoidal flux excitation to 1.3 and 1.4 T as indicated. Cores having a combination of 1.4 T /60Hz loss and exciting power at 25°C not greater than 0.27 W/kg and 0.9 VA/kg, respectively, are especiaUy preferred. Having thus described the invention in rather fuU detaU, it wiU be understood that this detail need not be strictly adhered to but that further changes and modifications may suggest themselves to one skilled in the art, aU falling within the scope of the invention as defined by the subjoined claims.

Claims: I . Λ metall ic alloy composed of iron, boron, si l icon, and carbon, hicrt is at lea.-vt about 70% amorphous, and w h ich consists essentially of the composition eatib^ic^' . wherein "a" - "d" are in atomic percent, the sum of "a", "b", "e". and "d" equals 100. "a" ranges from about 77 to 80. "b" ranges from about 7 to I 1 .5. "c" ranges from about 3 to 12. and "d" ranges from about 2 to 6, with the proviso that when "c" is greater than 7.5 "d" is at least about 4, said alloy having up to about 0.5 atomic percent of impurities and hav ing a cr stali i .aliou temperature of at least 5ϋl)°C. 2 The metallic alloy of claim I having a composition wherein "a" ranges from about 78 to SO and "b" ranges from about 8 to I I . 3. The metallic al loy of claim 6. hav ing a composition wherein "a" ranges Irom about 7° to 80, "b" ranges from about X. to 1 0.5, and "d" ranges from about 3 to 4.5. 4. The metallic alloy of claim 3, having a composition wherein "e" is al least about 6.5 5. The metall ic alloy of claim I , said alloy having been made by a process comprising the step of supply ing at least a portion of the boron consent o f said alloy from ferroboron. 6. The metallic alloy of claim 5, said ferroboron having been made In a carbothermic reduction process. 7 The metal l ic alloy of claim 1 , wherein the Curie temperature is at least about 360 U C, and the saturation magnetization corresponds to a magnetic mumen: of at lea.st about 165 emu.'g. 8. The metallic alloy of claim 7 wherein said Curie temperature is al lea.st about 3X0°C. l ). Λ gapped magnetic core comprising metal l ic strip formed of the adoy of claim 1 . wherein the al loy is at least about 'H ) % amorphous. 10. Λn article of manulaciurc comprising an alloy of claim 1 .

Inventors: FISH GORDON EDWARD, LIEBERMANN HOWARD HORST, RAMANAN V R V, SILGAILIS JOHN, FISH, GORDON, EDWARD, LIEBERMANN, HOWARD, HORST, RAMANAN, V., R., V., SILGAILIS, JOHN
Applicants: ALLIED SIGNAL INC, ALLIEDSIGNAL INC.
Application year: 1998
Main classification: C22C45
IPC codes: C22C45, H01F1