Patent Application
20240175112
The present disclosure relates to a steel wire for machine structural parts and a method for manufacturing the same.
In the manufacturing of various types of machine structural parts, such as automobile parts and construction machinery parts, bar steels including hot-rolled wire rods are usually subjected to spheroidizing annealing for the purpose of imparting cold-workability thereto. The steel wire obtained by the spheroidizing annealing is then subjected to cold working, followed by machining such as cutting, thereby forming a part with a predetermined shape. Further, a final strength adjustment is performed on the part by quenching and tempering, whereby a machine structural part is manufactured.
In recent years, there has been a demand for even softer steel wire than before in order to prevent cracking of steel material and improve the lifespan of dies during the cold working process.
As a method for obtaining a softened steel wire, for example, Patent Document 1 discloses a method for manufacturing a medium-carbon steel with excellent cold forgeability, which involves heating steel up to an austenitizing temperature range two or more times in the spheroidizing annealing process. According to the manufacturing method mentioned in Patent Document 1, it is indicated that a cold forgeable steel having a hardness of 83 HRB or less after the spheroidizing annealing and a spherical carbide ratio of 70% or more in the microstructure can be obtained.
Patent Document 2 discloses a steel material having low deformation resistance after the spheroidizing annealing and excellent cold forgeability, as well as a method for manufacturing the steel material. In the manufacturing method, steel satisfying a predetermined composition is hot-worked, cooled to room temperature and then has its temperature increased to a temperature range of A1 point to A1 point+50° C. After the temperature increase, it is held in the temperature range of the A1 point to A1 point+50° C. for 0 to 1 hour. Subsequently, after performing the annealing process two or more times by cooling at an average cooling rate of 10 to 200° C./hour from the temperature range of the A1 point to A1 point+50° C. to the temperature range of A1 point−100° C. to A1 point−30° C., the steel has its temperature increased to the temperature range from the A1 point to A1 point+30° C. and held in the temperature range from the A1 point to A1 point+30° C., followed by cooling. Specifically, after the temperature of the steel reaches the A1 point in increasing the temperature and held in the temperature range of the A1 point to A1 point+30° C., when cooling the steel, a dwell time in the temperature range of the A1 point to A1 point+30° C. until reaching the A1 point is set to a time between 10 minutes and 2 hours. The steel is cooled from the temperature range of the A1 point to A1 point+30° ° C. down to a cooling temperature range of A1 point−100° C. to A1 point−20° C. at an average cooling rate of 10 to 100° C./hour, followed by holding for 10 minutes to 5 hours in the cooling temperature range, and then it is further cooled.
Patent Document 3 discloses a steel wire for machine structural parts that can be lower deformation resistance during cold-working, improve the resistance to cracking, and exhibit excellent cold-workability. The steel wire has a predetermined composition, and the metallurgical microstructure of the steel is composed of ferrite and cementite, wherein the ratio of the number of cementite particles in the ferrite grain boundary is 40% or more of the number of all the cementite particles. Patent Document 3 describes the preferred manufacturing conditions for a rolled wire rod to be subjected to spheroidizing annealing as follows: finish rolling at 800° C. or higher and 1050° C. or lower; first cooling at an average cooling rate of 7° C./sec or more, second cooling at an average cooling rate of 1° C./sec or more and 5° C./sec or less, and third cooling at an average cooling rate more than the second cooling rate and also 5° C./sec or less, these cooling processes being performed in this order, with the end of the first cooling and the start of the second cooling in the range of 700 to 750° ° C., the end of the second cooling and the start of the third cooling in the range of 600 to 650° C., and the end of the third cooling at 400° C. or lower.
Patent Document 1: JP 2011-256456 A
Patent Document 2: JP 2012-140674 A
Patent Document 3: JP 2016-194100 A
However, the conventional technologies disclosed in Patent Documents 1 to 3 cannot sufficiently reduce the hardness of steel after the spheroidizing annealing, resulting in either inferior workability in cold-working performed after the spheroidizing annealing or inability to sufficiently enhance the hardness of steel in a quenching process performed after the cold-working, i.e., inferior quenching property. In other words, there is no conventional technology focusing on improving both the cold-workability and hardenability.
The present disclosure has been made in view of such circumstances and has an object to provide a steel wire for machine structural parts that has sufficiently low hardness and excellent cold-workability and can attain high hardness through a quenching process, that is, excellent hardenability, as well as a method for manufacturing a steel wire for machine structural parts that can manufacture the above-mentioned steel wire for machine structural parts in a relatively short period of time.
The terms “wire rod” and “steel bar” as used herein refer to rod-shaped and bar-shaped steel materials, respectively, obtained by hot rolling, and to which neither heat treatment such as spheroidizing annealing nor wire drawing is applied. The term “steel wire” refers to a wire rod or steel bar to which at least one of heat treatment such as spheroidizing annealing and wire drawing has been applied. Herein, the above wire rod, steel bar and steel wire are collectively referred to as a “bar steel”.
According to a first aspect of the prevent invention, there is provided a steel wire for machine structural parts, including:
In a second aspect of the prevent invention, there is provided the steel wire for machine structural parts according to the first aspect, further including one or more selected from the group consisting of:
In a third aspect of the prevent invention, there is provided the steel wire for machine structural parts according to the first or second aspect, further including one or more selected from the group consisting of:
In a fourth aspect of the prevent invention, there is provided the steel wire for machine structural parts according to any one of the first to third aspects, further including one or more selected from the group consisting of:
In a fifth aspect of the prevent invention, there is provided the steel wire for machine structural parts according to any one of the first to fourth aspects, wherein an average ferrite grain size is 30 μm or less.
According to a sixth aspect of the prevent invention, there is provided a method for manufacturing the steel wire for machine structural parts according to any one of the first to fifth aspects, the method including: subjecting a bar steel satisfying the chemical composition according to any one of the first to fourth aspects to spheroidizing annealing, the spheroidizing annealing including the following processes (1) to (3):
A1 (° C.)=723+29.1×[Si]−10.7×[Mn]+16.9×[Cr]−16.9×[Ni] (1)
where an expression [element] represents the content of each element (% by mass), and the content of an element not contained is zero.
In a seventh aspect of the prevent invention, there is provided the method for manufacturing the steel wire for machine structural parts according to the sixth aspect, wherein the bar steel is a steel wire obtained by subjecting a wire rod to wire drawing at an area reduction ratio of more than 5%.
According to the present disclosure, a steel wire for machine structural parts with excellent cold-workability and excellent hardenability and a method for manufacturing the steel wire for machine structural parts can be provided.
The present inventors have intensively studied steel wires in order to realize a steel wire for machine structural parts that is excellent in terms of cold-workability and hardenability. As a result, the present inventors have found that it is desirable to set the ratio of the total content of Mn and Cr in cementite to the total content of Mn and Cr in steel at a certain level or more and to set an average size of all the cementite within a certain range depending on the C content of the steel. Furthermore, in order to realize the above metallurgical microstructure, the inventors have also found that it is effective to cause the metallurgical microstructure to have a chemical composition within a certain range and to perform spheroidizing annealing particularly on the specified conditions in the method for manufacturing the steel wire for machine structural parts. Hereinafter, a description will be given on the steel wire for machine structural parts according to the present embodiment, especially, the metallurgical microstructure of the steel wire for machine structural parts.
Conventionally, steel material is subjected to spheroidizing annealing to form a metallurgical microstructure composed of ferrite and cementite, thereby ensuring the cold-workability. However, this metallurgical microstructure cannot achieve either more excellent cold-workability or hardenability. For this reason, the present inventors have studied intensively from various angles in order to realize a steel wire for machine structural parts that achieves both excellent cold-workability and excellent hardenability. First, the inventors have focused on the Mn content and Cr content in cementite. For example, when the spheroidizing annealing is performed on manufacturing conditions mentioned below to set an average size of all the cementite at a certain level or more and to increase the Mn content and Cr content in the cementite, the Mn content and Cr content in ferrite can be relatively decreased, thus suppressing hardening due to solid-solution strengthening and making it possible to achieve low hardness, leading to the improvement in the cold-workability. In addition, the inventors have found that by suppressing the average size of all the cementite to the certain level or less, the undissolved cementite can be suppressed while the high temperature is held in the quenching process, thereby improving the hardenability. There is no technology that focuses on both the Mn content and Cr content of the cementite and the average size of all the cementite.
[When the total content of Cr and Mn (% by mass) in the cementite is expressed as {Cr+Mn}, the total content of Cr and Mn (% by mass) in the steel is expressed as [Cr+Mn], and the C content (% by mass) of the steel is expressed as [C], the concentration ratio {Cr+Mn}/[Cr+Mn] is (0.5 [C]+0.040) or more]
Cr and Mn are typical elements that tend to be solid-soluble in cementite. However, some of them are solid-soluble in ferrite, and the more the amount of solid-solution of them in the ferrite, the stronger the ferrite matrix becomes, resulting in increased hardness. Therefore, the larger the ratio of the total content {Cr+Mn} of Cr and Mn in the cementite to the total content [Cr+Mn] of Cr and Mn in the steel, i.e., the larger the concentration ratio {Cr+Mn}/[Cr+Mn], the less the total content of Cr and Mn in ferrite occupying phases other than cementite can become. As a result, the solid-solution strengthening amount of ferrite due to Cr and Mn is decreased, and along with this, the hardness is reduced, improving the cold-workability. Because of the influence of the C content of the steel, the lower limit of the concentration ratio {Cr+Mn}/[Cr+Mn] is set to (0.5 [C]+0.040) or more when the C content of the steel is expressed as [C] (% by mass) . The concentration ratio {Cr+Mn}/[Cr+Mn] is preferably (0.5[C]+0.042) or more. Meanwhile, when taking into consideration of implementable manufacturing conditions and the like, the upper limit of the concentration ratio {Cr+Mn}/[Cr+Mn] is approximately 0.5[C]+0.500.
With regard to the above cementite, its form is not particularly limited and includes spherical cementite as well as bar-shaped cementite with a large aspect ratio. The aspect ratio is the ratio (major diameter/minor diameter) of the longest length of a cementite particle, the major diameter, to the longest length in the direction perpendicular to the major diameter, the minor diameter. The size standard of cementite to be measured is not limited, but the smallest size is defined as the size of cementite in which the total content of Cr and Mn can be measured as shown in the examples below. Specifically, when electrolytic extraction residue measurement is performed by a method shown in examples mentioned below, cementite remaining on a filter with a pore size of 0.10 μm is the target of the measurement. The total content of Cr and Mn in the steel is the sum of the average Cr content and the average Mn content in the steel as shown in the examples mentioned below. For example, when the metallographic microstructure is composed of ferrite and cementite, this total content of Cr and Mn refers to the total content of Cr and Mn in ferrite and cementite in % by mass.
[When a C content (% by mass) of the steel is expressed as [C], the average circular-equivalent diameter of all the cementite is (1.668-2.13 [C]) μm or more and (1.863-2.13 [C]) μm or less]
In the case of the cementite content of the steel being constant, the larger the size of the cementite, the smaller the number density of cementite and the longer the distance between the cementite particles. The longer the distance between the cementite particles in the steel, the more difficult the precipitation strengthening is to perform, and consequently the hardness of the steel can be reduced. The effect of reducing the hardness by enhancing the total content of Cr and Mn in the cementite can be easily exhibited by setting the size of the cementite at the certain level or more. From these viewpoints, when the C content (% by mass) of the steel is expressed as [C], the present disclosure sets the average circular-equivalent diameter of all the cementite to be (1.668-2.13 [C]) um or more. The average circular-equivalent diameter of all the cementite is preferably (1.669-2.13 [C]) μm or more. On the other hand, when the cementite is excessively coarse, the cementite does not dissolve sufficiently when held at a high temperature in a quenching process after cold-working, which cannot obtain a sufficiently high hardness through the quenching. Therefore, in the present disclosure, the average circular-equivalent diameter of all the cementite is set to (1.863-2.13 [C]) μm or less. It is preferably (1.858-2.13 [C]) μm or less.
In Patent Document 3, it is indicated that cementite present at the ferrite grain boundaries receives less strain during cold-workability than cementite present in the ferrite grains, which reduces deformation resistance. However, the average size of all the cementite is not controlled in Patent Document 3, and as a result, the cementite cannot be sufficiently dissolved while holding it at a high temperature in the quenching process, resulting in inferior hardenability. The present disclosure is directed to a technology focusing on both the ratio of the total content of Cr and Mn in the cementite and the average size of all the cementite in order to realize a steel wire for machine structural parts with excellent cold-workability and excellent hardenability.
The metallurgical microstructure of the steel wire for machine structural parts according to the present embodiment, which is a spheroidized microstructure having spheroidized cementite, can be obtained by subjecting the bar steel, which satisfies the chemical composition to be mentioned later, to spheroidizing annealing to be mentioned later, for example.
The metallurgical microstructure of the steel wire for machine structural parts of the present embodiment is substantially composed of ferrite and cementite. The above “substantially” means that the area ratio of ferrite in the metallurgical microstructure of the steel wire for machine structural parts of the present embodiment is 90% or more, while allowing the area ratio of bar-shaped cementite with an aspect ratio of 3 or more in the metallurgical microstructure to be 5% or less, and also allowing the area ratio of nitrides such as AlN and inclusions other than nitrides to be less than 3% if they hardly adversely affect the cold-workability. Further, the area ratio of the ferrite may be 95% or more.
The term “ferrite” as used herein refers to a portion in which the crystal structure has a bcc structure, and it includes ferrite in pearlite which has a layered structure of ferrite and cementite.
The term “ferrite grains” to be measured for “ferrite grain size” includes, as an evaluation target, crystal grains containing bar-shaped cementite that are formed during spheroidizing annealing due to insufficient spheroidizing, but it does not include, as the target, crystal grains containing bar-shaped cementite (pearlite grains) that have remained since before the spheroidizing annealing. Specifically, it refers to “crystal grains having no cementite in the grains” and “crystal grains having cementite in the grains and in which the shape of cementite can be observed (i.e., the boundary between the cementite and the ferrite can be clearly observed)”, all of which can be confirmed when observed at a magnification of 1,000 times using an optical microscope after etching with nital (2% by volume nitric acid and 98% by volume ethanol). Crystal grains in which the shape of cementite cannot be observed at a magnification of 1,000 times using the optical microscope (i.e., in which the boundary between the cementite and ferrite cannot be observed clearly) are not to be judged in the present embodiment, and thus are not included in the “ferrite grains”.
The steel wire for machine structural parts according to the present embodiment preferably has an average ferrite grain size of 30 μm or less in the metallurgical microstructure. When the average ferrite grain size is 30 μm or less, the ductility of the steel wire for machine structural parts can be improved, further suppressing the occurrence of cracking during cold-working. The average ferrite grain size is more preferably 25 μm or less, and even more preferably 20 μm or less. The smaller the average ferrite grain size, the more preferred it is, but the lower limit of the average ferrite grain size may be approximately 2 μm in consideration of implementable manufacturing conditions and the like.
The steel wire for machine structural parts according to the present embodiment, which satisfies the following chemical composition and has the metallurgical structure mentioned above, can achieve both low hardness that allows good cold-working and high hardness after a quenching process. In the present embodiment, when the C content (% by mass), Cr content (% by mass), and Mo content (% by mass) in the steel are expressed as [C], [Cr], and [Mo], respectively (the content of an element not contained is zero % by mass), in a case where the hardness, i.e., the hardness of the steel after the spheroidizing annealing in Examples mentioned below, satisfies the following equation (2) while the hardness after the quenching process satisfies the following equation (3), it is determined that the hardness is sufficiently low to achieve excellent cold-workability, and high hardness after the quenching process, i.e., excellent hardenability is achieved.
Hardness (after spheroidizing annealing) (HV)<91 ([C]+[Cr]/9+[Mo]/2)30 91 (2)
Hardness after the quenching process (HV)>380 ln ([C])+1010 (3)
The chemical composition of the steel wire for machine structural parts according to the present embodiment will be described.
C is an element that controls the strength of steel material, and the higher its content, the higher the strength of the steel after quenching and tempering. In order to effectively exhibit the above effect, the lower limit of the C content is set to 0.05% by mass. The C content is preferably 0.10% by mass or more, more preferably 0.15% by mass or more, and even more preferably 0.20% by mass or more. However, if the C content is excessive, the number of spherical cementite particles in the microstructure after the spheroidizing annealing becomes excessive, and the hardness increases, resulting in reduced cold-workability. Therefore, the upper limit of the C content is set to 0.60% by mass. The C content is preferably 0.55% by mass or less, and more preferably 0.50% by mass or less.
Si is used as a deoxidizer during smelting and also contributes to the improvement in the strength. In order to effectively exhibit this effect, the lower limit of the Si content is set to 0.005% by mass. The Si content is preferably 0.010% by mass or more, and more preferably 0.050% by mass or more. However, Si contributes to solid solution strengthening of ferrite and has the action of considerably enhancing the strength after the spheroidizing annealing. If the Si content is excessive, the cold-workability is degraded due to the above action, and therefore the upper limit of the Si content is set to 0.50% by mass. The Si content is preferably 0.40% by mass or less, and more preferably 0.35% by mass or less.
Mn is an element that effectively acts as a deoxidizer and also contributes to the improvement in the hardenability. In order to sufficiently exhibit this effect, the lower limit of the Mn content is set to 0.30% by mass. The Mn content is preferably 0.35% by mass or more, and more preferably 0.40% by mass or more. However, if the Mn content is excessive, segregation occurs more easily, resulting in a reduced toughness. Thus, the upper limit of the Mn content is set to 1.20% by mass. The Mn content is preferably 1.10% by mass or less, and more preferably 1.00% by mass or less.
P (phosphorus) is an inevitable impurity and a harmful element that causes the grain boundary segregation in the steel, adversely affecting forgeability and toughness. Thus, the P content is 0.050% by mass or less. The P content is preferably 0.030% by mass or less, and more preferably 0.020% by mass or less. The smaller the P content, the more preferred it is, and the P content is usually 0.001% by mass or more.
S (sulfur) is an inevitable impurity that forms MnS in the steel to degrade ductility, and is thus a disadvantageous element for cold-workability. Thus, the S content is 0.050% by mass or less. The S content is preferably 0.030% by mass or less, and more preferably 0.020% by mass or less. The smaller the S content, the preferred it is, but the S content is usually 0.001% by mass or more.
Al is an element included as a deoxidizer and has the effect of reducing impurities along with deoxidation. To exhibit this effect, the lower limit of the Al content is set to 0.001% by mass. The Al content is preferably 0.005% by mass or more, and more preferably 0.010% by mass or more. However, if the Al content is excessive, the amount of non-metallic inclusions increases, and the toughness is reduced. Thus, the upper limit of the Al content is set to 0.10% by mass. The Al content is preferably 0.08% by mass or less, and more preferably 0.05% by mass or less.
Cr is an element that has the effect of improving the hardenability of steel and enhancing its strength, and also has the effect of promoting the spheroidizing of cementite. Specifically, Cr is solid-soluble in cementite and delays the dissolution of cementite during heating in the spheroidizing annealing. A portion of cementite remains without dissolving during heating, so that bar-shaped cementite with a large aspect ratio is less likely to be formed during cooling, making it easier to obtain a spheroidized microstructure. Therefore, the Cr content is more than 0% by mass and preferably 0.01% by mass or more. Furthermore, it may be 0.05% by mass or more, and even more 0.10% by mass or more. From the viewpoint of further promoting spheronization of cementite, the Cr content can be more than 0.30% by mass, and can be further more than 0.50% by mass. If the Cr content is excessive, the diffusion of elements containing carbon is delayed, and the dissolution of cementite is delayed more than necessary, making it difficult to obtain a spheroidized microstructure. As a result, the effect of reducing the hardness according to the present invention can be reduced. Thus, the Cr content is 1.50% by mass or less, preferably 1.40% by mass or less, and more preferably 1.25% by mass or less. From the viewpoint of faster diffusion of the elements, the Cr content can further be 1.00% by mass or less, 0.80% by mass or less, and even 0.30% by mass or less.
N is an impurity inevitably contained in the steel, but a large content of solid solution N in the steel leads to an increase in the hardness and a decrease in ductility due to strain aging, degrading the cold-workability. Therefore, the N content is 0.02% by mass or less, preferably 0.015% by mass or less, and more preferably 0.010% by mass or less.
The balance is iron and inevitable impurities. As inevitable impurities, trace elements (e.g., As, Sb, Sn, etc.) brought in due to conditions of raw materials, materials, manufacturing facilities, and the like are permitted to be mixed in the steel. For example, there are elements such as P and S, which are usually preferred in smaller contents and are therefore inevitable impurities, but whose composition range is separately specified above. For this reason, the term “inevitable impurities” constituting the balance herein is based on the concept that an element whose composition range is individually specified is excluded.
The chemical composition of the steel wire for machine structural parts according to the present embodiment only needs to contain the above-mentioned elements. The selected elements mentioned below do not need to be included, but by including them together with the above elements as necessary, the hardenability and the like can be ensured more easily. The selected elements will be described below.
[One or more selected from the group consisting of Cu: more than 0% by mass and 0.25% by mass or less, Ni: more than 0% by mass and 0.25% by mass or less, Mo: more than 0% by mass and 0.50% by mass or less, and B: more than 0% by mass and 0.01% by mass or less]
Cu, Ni, Mo, and B are all elements effective in increasing the strength of final products by improving the hardenability of the steel material. They may be contained alone or in combination of two or more kinds as necessary. The effects of these elements increase as their contents increase. To effectively exhibit the above effects, the preferred lower limit of the content of each of Cu, Ni, and Mo is more than 0% by mass, more preferably 0.02% by mass or more, and even more preferably 0.05% by mass or more, and the preferred lower limit of the B content is more than 0% by mass, more preferably 0.0003% by mass or more, and even more preferably 0.0005% by mass or more.
On the other hand, if the contents of these elements are excessive, the strength of the steel may become extremely high, and the cold-workability may be degraded. Thus, the preferred upper limit of each of these elements is set as mentioned above. More preferably, the content of each of Cu and Ni is 0.22% by mass or less, and even more preferably 0.20% by mass or less; the Mo content is more preferably 0.40% by mass or less, even more preferably 0.35% by mass or less; and the B content is more preferably 0.007% by mass or less, and even more preferably 0.005% by mass or less.
[One or more selected from the group consisting of Ti: more than 0% by mass and 0.2% by mass or less, Nb: more than 0% by mass and 0.2% by mass or less, and V: more than 0% by mass and 0.5% by mass or less]
Ti, Nb, and V each form a compound with N to reduce solid solution N, thereby exhibiting the effect of reducing deformation resistance. Thus, they can be contained alone or in combination of two or more kinds as necessary. The effects of these elements increase as their contents increase. To effectively exhibit the above-mentioned effects, the preferred lower limit of the content of any of these elements is more than 0% by mass, more preferably 0.03% by mass or more, and even more preferably 0.05% by mass or more. However, if the contents of these elements are excessive, the compounds formed may increase the deformation resistance, which in turn may reduce the cold-workability. Thus, the content of each of Ti and Nb is preferably 0.2% by mass or less, and the V content is preferably 0.5% by mass or less. The content of each of Ti and Nb is more preferably 0.18% by mass or less, and even more preferably 0.15% by mass or less, and the V content is more preferably 0.45% by mass or less, and even more preferably 0.40% by mass or less.
[One or more selected from the group consisting of Mg: more than 0% by mass and 0.02% by mass or less, Ca: more than 0% by mass and 0.05% by mass or less, Li: more than 0% by mass and 0.02% by mass or less, and Rare Earth Metal (REM) : more than 0% by mass and 0.05% by mass or less]
Mg, Ca, Li, and REM are elements effective in spheroidizing sulfide-based inclusions such as MnS and improving the deformation capacity of steel. These actions become more effective as their contents increase. To effectively exhibit the above-mentioned effects, the content of each of Mg, Ca, Li, and REM is preferably more than 0% by mass, more preferably 0.0001% by mass or more, and even more preferably 0.0005% by mass or more. However, even when their contents are excessive, their effects are already saturated, and no additional effects corresponding to their contents can be expected. Thus, the content of each of Mg and Li is preferably 0.02% by mass or less, more preferably 0.018% by mass or less, and even more preferably 0.015% by mass or less, and the content of each of Ca and REM is preferably 0.05% by mass or less, more preferably 0.045% by mass or less, and even more preferably 0.040% by mass or less. It is noted that Mg, Ca, Li and REM may be contained alone or in combination with two or more kinds. When two or more kinds of them are contained, the content of each element may be any content within the above-mentioned range. The term REM means lanthanide elements (15 elements from La to Lu), Sc (scandium) and Y (yttrium).
The shape or the like of the steel wire for machine structural parts according to the present embodiment is not particularly limited. For example, the steel wire has a diameter of 5.5 mm to 60 mm.
In order to obtain the metallurgical microstructure of the steel wire for machine structural parts according to the present embodiment, it is preferable to appropriately control the conditions for the spheroidizing annealing in the manufacturing of the steel wire for machine structural parts as follows. A hot rolling process for manufacturing a wire rod or steel bar to be subjected to the spheroidizing annealing is not particularly limited and can be performed by established methods. As mentioned later, wire drawing may be applied prior to the spheroidizing annealing. The diameter of the wire rod, steel wire, or steel bar, which is a bar steel to be subjected to the spheroidizing annealing, is not particularly limited. For the wire rod or steel wire, the diameter thereof is, for example, 5.5 mm to 55 mm. For the steel bar, the diameter thereof is, for example, 18 mm to 105 mm.
Referring to
The method for manufacturing the steel wire for machine structural parts according to the embodiment of the present invention includes the spheroidizing annealing process including the following processes (1) to (3):
A1 (° C.)=723+29.1×[Si]−10.7×[Mn]+16.9×[Cr]−16.9×[Ni] (1)
[(1) Heating the steel to the temperature T1 of (A1+8° C.) to (A1+31° C.), and then heating and holding the steel at the temperature T1 for more than 1 hour and 6 hours or less ([2] in
By heating to the temperature T1 of (A1+8° C.) to (A1+31° C.), the dissolution of bar-shaped cementite with a large aspect ratio, which has been formed during the rolling stage, is promoted. If the temperature T1 is extremely low, the bar-shaped cementite is not dissolved during heating and holding and remains in ferrite grains, resulting in an increased hardness. To obtain sufficiently softened steel wires, the temperature T1 needs to be set to (A1+8° C.) or higher. The temperature T1 is preferably (A1+15° C.) or higher, and more preferably (A1+20° C.) or higher. On the other hand, if the temperature T1 is extremely high, the crystal grains become excessively coarse, making it more difficult to precipitate spherical cementite at the ferrite grain boundaries during the subsequent cooling process, and increasing the amount of bar-shaped cementite, resulting in an increased hardness. Therefore, the temperature T1 is set to (A1++31° C.) or lower. The temperature T1 is preferably (A1++30° C.) or lower, and more preferably (A1++29° C.) or lower.
If the heat holding time (t1) at the temperature T1 is extremely short, bar-shaped cementite remains in the ferrite grains, and the hardness increases. To obtain sufficiently softened steel wires, the heat holding time (t1) needs to be more than 1 hour and 6 hours or less. The preferred heat holding time (t1) is 1.5 hours or more, and more preferably 2.0 hours or more. If the heat holding time (t1) is extremely long, the heat treatment time becomes longer, thus reducing the productivity. Thus, the heat holding time (t1) is 6 hours or less, preferably 5 hours or less, and more preferably 4 hours or less. The average temperature increase rate during heating to the temperature T1 of (A1+8° C.) to (A1+31° C.) ([1] of
It is noted that the temperature at the above-mentioned A1 point is calculated by the following equation (1) mentioned on p. 273, Leslie, W. C. The Physical Metallurgy of Steels (Maruzen) .
A1 (° C.)=723+29.1×[Si]−10.7×[Mn]+16.9×[Cr]−16.9×[Ni] (1)
[(2) Performing a cooling-heating process two to six times in total, wherein the cooling-heating process includes cooling the steel to the temperature T2 of higher than 650° C. and (A1−17° C.) or lower, and then heating the steel to the temperature T3 of (A1+8° C.) to (A1+31° C.) at a temperature increase rate of 75° C./hour to 160° C./hour ([3] to [7] in
After the process (1) of heating and holding, the steel is cooled to the temperature T2 of higher than 650° C. and (A1−17° C.) or lower in order to promote the precipitation of cementite whose concentration of Mn and Cr is high. If the temperature T2 is extremely low, the annealing time becomes longer. In addition, if the temperature T2 is extremely low, cementite becomes excessively fine, so that cementite whose content of Cr and Mn is small is formed easily. Therefore, the ultimate temperature T2 of the cooling needs to be higher than 650° C. According to the manufacturing method of the present embodiment, even when the ultimate temperature T2 of the cooling is higher than 650° ° C., desired cementite can be obtained without performing the annealing for a long time. The temperature T2 is preferably 670° C. or higher. On the other hand, if the temperature T2 is extremely high, cementite is not reprecipitated sufficiently, and consequently, Cr and Mn are not sufficiently enriched in the cementite, whereby the total content of Cr and Mn in the cementite becomes small, and the hardness increases, thus reducing the cold-workability. Therefore, the upper limit of the temperature T2 is set to A1−17° C. The temperature T2 is preferably A1−18° C. or lower. In addition, if the temperature T2 is reached and then held, this leads to a longer heat treatment time. Therefore, from these viewpoints, the steel should not be held at the temperature T2. However, it may be held only for a short time so as to make variations in the temperature of the inside of a furnace uniform. The holding time (t2) at the ultimate temperature T2 of the cooling is preferably 1 hour or less.
It is noted that the average cooling rate during cooling ([3] in
(2-ii) Heating the steel to the temperature T3 of (A1+8° C.) to (A1+31° C.) at the average temperature increase rate of 75° C./hour to 160° C./hour ([5] and [6] in
In order to increase the content of Cr and Mn in the cementite precipitated during the process (2-i) of cooling, the steel is heated from the temperature T2 to the temperature T3 of (A1+8° C.) to (A1+31° C.) at an average temperature increase rate R of 75° C./hour to 160° C./hour. If the average temperature increase rate R is extremely fast, the diffusion of Cr and Mn becomes insufficient, and the content of Cr and Mn in the cementite formed during heating and holding the temperature becomes deficient, resulting in an increased hardness and reduced cold-workability.
Therefore, the average temperature increase rate R is set to 160° C./hour or less. The average temperature increase rate R is preferably 155° ° C./hour or less, and more preferably 150° C./hour. It is even more preferably 120° C./hour or less, and particularly preferably 100° C./hour or less. On the other hand, if the average temperature increase rate R is extremely slow, cementite dissolves more than necessary, and as a result, the total content of Cr and Mn contained in the cementite decreases. Furthermore, if the average temperature increase rate R is extremely slow, cementite formed during the cooling from the temperature T1 is excessively coarsened, and consequently, cementite cannot dissolve sufficiently while the high temperature is held in the quenching process, resulting in a lower hardness after the quenching process, i.e., degraded hardenability. This further leads to a longer annealing time and reduced productivity. Therefore, the average temperature increase rate R is set to 75° C./hour or more, and preferably 80° C./hour or more.
If the temperature T3, which is an ultimate temperature of heating in the cooling-heating process, is extremely low, the diffusion of Cr and Mn becomes insufficient, and the content of Cr and Mn in the cementite formed during heating and holding the temperature becomes deficient, resulting in an increased hardness and reduced cold-workability. Therefore, the temperature T3 needs to be (A1+8° C.) or higher. The temperature T3 is preferably (A1+15° C.) or higher, and more preferably (A1+20° C.) or higher. On the other hand, if the temperature T3 as the ultimate temperature of heating is extremely high, the cementite dissolves more than necessary, resulting in a decrease in the total content of Cr and Mn in the cementite. Therefore, the ultimate temperature (T3) of heating is set to (A1+31° C.) or lower. The temperature T3 is preferably (A1+30° C.) or lower, and more preferably (A1+29° C.) or lower.
After the temperature T3 as the ultimate temperature of heating is reached, the steel may be held at the temperature
T3. However, if a holding time (t3) at the temperature T3 is extremely long, spherical cementite formed in the heat holding step at the temperature T1 may easily redissolve, leading to an increase in the hardness. If the holding time (t3) at the temperature T3 is extremely long, the annealing time becomes longer, which may reduce the productivity. Thus, the holding time (t3) at the temperature T3 is preferably one hour or less.
In the manufacturing method according to the present embodiment, as mentioned below, the cooling-heating process including the cooling in the process (2-i) and the heating in the process (2-ii) is performed a plurality of times. In each time, the temperature T2 as the ultimate temperature of the cooling, the average temperature increase rate R and the temperature T3 need to satisfy the above-mentioned ranges.
The magnitude relationship between the temperature T3 and the temperature T1 is not particularly limited, but for example, the temperature T3 may be the same as the temperature T1, or the temperature T3 may be higher than the temperature T1. Alternatively, the temperature T1 may be higher than the temperature T3 from the viewpoint of making bar-shaped cementite sufficiently solid-soluble in austenite. (2-iii) Performing of the cooling-heating process two to six times in total ([7] of
To increase the concentration of Mn and Cr in the cementite and to promote the coarsening of the cementite, the above-mentioned cooling-heating process needs to be performed two to six times in total. If the above-mentioned cooling-heating process is not repeated, the concentration of Mn and Cr in the cementite becomes insufficient, or the coarsening of cementite becomes insufficient. As a result, the hardness of the steel after the spheroidizing annealing increases. Thus, the above-mentioned cooling-heating process is performed two or more times. Preferably, it is performed three or more times. The more times the process is performed, the lower the hardness becomes, but if the process is performed extremely many times, its effect is saturated. In addition, this leads to a longer annealing time, reducing the productivity. Therefore, the number of times the cooling-heating process is performed is set to six or less. In the case of
[(3) Cooling the steel from the temperature T3 of the final cooling-heating process ([8] of
The steel is cooled from the temperature T3 of the final cooling-heating process. The average cooling rate and the ultimate cooling temperature during the cooling are not particularly limited. From the viewpoint of further suppressing the reprecipitation of bar-shaped cementite, the average cooling rate may be set to 100° C./hour or lower, for example. The average cooling rate may be set to 5° C./hour or higher from the viewpoint of further suppressing excessive coarsening of cementite. The ultimate cooling temperature can be, for example, (A1-30° C.) or lower. For example, the steel may be cooled at the above average cooling rate to a temperature range of (A1-30° C.) or lower and (A1 -)100° ° C. or higher, followed by air cooling. Alternatively, for example, the ultimate cooling temperature may be set to lower than (A1−100° C.) to further suppress the reprecipitation of the bar-shaped cementite and further enhance the cold-workability. In this case, from the viewpoint of shortening the annealing time, the ultimate cooling temperature may be (A1−250° ° C.) or higher, further (A1−200° ° C.) or higher, or even (A1−150° C.) or higher.
The above-mentioned spheroidizing annealing (processes (1) to (3)) may be repeated one or more times. From the viewpoint of preventing excessive coarsening of cementite and ensuring productivity, the annealing is preferably performed four times or less, and more preferably three times or less. When the above-mentioned spheroidizing annealing is repeated a plurality of times, it may be repeated on the same conditions or under different conditions within the above specified range. When the above-mentioned spheroidizing annealing is repeated a plurality of times, wire drawing may be added between the spheroidizing annealing processes. For example, wire drawing prior to the spheroidizing annealing, which is mentioned later,→first spheroidizing annealing→wire drawing→second spheroidizing annealing can be performed in this order.
In the method for manufacturing the steel wire for machine structural parts according to the present embodiment, processes other than the spheroidizing annealing process are not particularly limited. For example, after the spheroidizing annealing, performing wire drawing at an area reduction ratio of preferably 15% or less may be included for the purpose of adjusting dimensions. By setting the area reduction ratio to 15% or less, the increase in the hardness prior to the cold-working can be suppressed. The area reduction ratio is more preferably 10% or less, further preferably 8% or less, and even more preferably 5% or less.
To promote the formation of the microstructure form of the present invention, subjecting the wire rod to wire drawing at the area reduction ratio of more than 5% prior to the spheroidizing annealing is preferably included. By performing the wire drawing at the above-mentioned area reduction ratio, the cementite in the steel is broken down, and the aggregation of cementite in the subsequent spheroidizing annealing process can be promoted, so that cementite can be appropriately coarsened, which is effective in softening the steel. Further, by performing the wire drawing at the above-mentioned area reduction ratio, migration of an interface and diffusion of elements become more active, resulting in an increase content of Cr and Mn in the cementite. The area reduction ratio is more preferably 10% or more, further preferably 15% or more, and even more preferably 20% or more. On the other hand, an excessively large area reduction ratio can cause a risk of wire breakage. Thus, the area reduction ratio is preferably set to 50% or less. In the case of performing the wire drawing a plurality of times, the number of execution of wire drawing is not particularly limited, and can be, for example, two. When the wire drawing is performed a plurality of times, the term “area reduction ratio during the wire drawing” means the area reduction ratio of a steel material obtained after the wire drawing is repeated a plurality of times to the steel material prior to the wire drawing.
Hereinafter, the present disclosure will be described more specifically by way of Examples. The present disclosure is not limited by the following Examples, but obviously it may also be implemented with modifications as appropriate to the extent that the modifications conform to the above-mentioned and following concepts, and all of these modifications are included in the technical scope of the present disclosure.
After specimens with the chemical compositions shown in Table 1 were smelted in a converter furnace, steel pieces obtained by casting were hot-rolled, thereby manufacturing wire rods with diameters of 12 to 16 mm. In Table 2 mentioned later, in the case of “presence” of the wire drawing prior to the spheroidizing annealing, i.e., in sample No. 2 as shown in Table 3 which was manufactured under the manufacturing conditions B, a steel wire obtained by wire drawing of the wire rod at the area reduction ratio of 25% was subjected to spheroidizing annealing.
The above wire rod or steel wire was used and annealed using a laboratory furnace. In the annealing, the wire rod or steel wire had its temperature increased up to Tl shown in Table 2 and held for tl hours. The wire rod or steel wire was then cooled to the temperature T2 in Table 2 at the average cooling rate of 5 to 100° C./hr, and subsequently heated to the temperature T3 at the average temperature increase rate R shown in Table 2. This cooling-heating process was performed the number of execution of the cooling-heating shown in Table 2. Then cooling from the heating temperature of the final cooling-heating process was performed to produce a sample.
As Comparative Example, sample No. 12 shown in Table 3 was obtained under a manufacturing condition H1, in which a heat treatment process shown in
As another Comparative Example, sample No. 14 shown in Table 3 was obtained under a manufacturing condition I, in which a heat treatment process was performed under heat treatment conditions satisfying the manufacturing conditions of Patent Document 3, in detail, under the conditions indicated as SA2 in an example of Patent Document 3, that means the heat treatment process shown in
T1, T2, and T3, which were annealing parameterss described in Table 2, were the set temperatures of the heat treatment furnace. The deviation between the actual temperature of the steel material and the set temperature was tested by attaching thermocouples to the steel material, and it was confirmed that the temperature of the steel material was substantially the same as the set temperature.
Using the samples obtained by the above annealing process, the average ferrite grain size, the average size of all the cementite, and the total content of Cr and Mn in the cementite were determined in the following ways as evaluation items of the metallurgical microstructure. In addition, the hardness after the spheroidizing annealing and the hardness after the quenching process were measured and evaluated as the properties by the following methods.
First, the ferrite grain size number was measured as follows. A test piece was embedded in resin such that the D/4 position (D: diameter of a steel wire) of the cross-section of the steel wire after the spheroidizing annealing, i.e., the section perpendicular to the axial direction of the steel wire, could be observed, and the above test piece was etched using nital (2% by volume nitric acid and 98% by volume ethanol) as a corrosion solution to expose its microstructure. The above exposed microstructure of the test piece was observed with an optical microscope at a magnification of 400 times, and one field of view where ferrite crystal grains of an average size, representative of the microstructure of the entire steel wire, could be observed was selected in an evaluation plane, whereby its micrograph was obtained. The value of the ferrite grain size number (G) was then calculated based on a comparison method of JIS G0551 (2020) from the micrographs taken. Subsequently, by using the calculated value of the ferrite grain size number (G), an average ferrite grain size dn was determined from the following equation (4), wherein the equation shows the relationship between the average ferrite grain size dn and the ferrite grain size number G (or N) among the relationships between various quantities regarding the grain size number and grain size, described in Table 1 on p. 32 of “Introductory Course Technical Terms—Iron and Steel Materials Edition-3: Grain Size Numbers and Grain Sizes,” Minoru Umemoto, Ferrum Vol. 2 (1997) No. 10, pp. 29-34. The results are shown in Table 3. It is noted that in the present examples, the samples Nos. 1 to 11 in Table 3 all had an area ratio of ferrite of 90% or more.
dn=0.254/(2(G−1)/2) (4)
To measure the average size of all the cementite of the steel wire after the spheroidizing annealing, a test piece was embedded in resin such that the cross-section of the steel wire could be observed, followed by cutting, and a cut surface of the test piece was mirror polished by emery paper and diamond buffing. The cut surface was then etched for 30 seconds to 1 minute using nital (2% by volume nitric acid and 98% by volume ethanol) as the corrosion solution to expose the ferrite grain boundaries and cementite at the D/4 position (D: diameter of the steel wire). Subsequently, the microstructure of the test piece with the above-mentioned cementite, etc. being exposed was observed using a field-emission scanning electron microscope (FE-SEM), and three fields of view were taken at a magnification of 2,500 times.
An OHP film was superimposed on the micrograph taken above, and all the cementite of the micrograph was filled in from above the OHP film to thereby obtain a projected image for the analysis. The projected image was binarized to form a black-and-white photograph, and the circular-equivalent diameter of all the cementite was calculated using an image package software “Particle Analysis Ver. 3.5” (manufactured by NIPPON STEEL TECHNOLOGY Co., Ltd.). It is noted that the average size of all the cementite mentioned in Table 3 is the average value calculated from the three fields of view. The minimum size (circular-equivalent diameter) of cementite to be measured was 0.3 μm.
A specimen was fabricated by cutting or polishing a steel wire from an area of the steel wire except for its superficial layer portion (of less than 1 mm) so as to enable electrolysis of a sample of about 9 g. The specimen was immersed in an electrolytic solution (10% acetylacetone-1% tetramethylammonium chloride-methanol) and energized to conduct constant-current electrolysis on about 9 g of the above specimen. Thereafter, the electrolytic solution after the electrolysis was then filtered through a filter with a pore diameter of 0.10 μm (polycarbonate-type membrane filter, manufactured by Advantec Toyo Kaisha, Ltd.) to obtain the residue remaining on the filter as cementite in the steel. The above residue was then dissolved in an acid solution and analyzed by ICP optical emission spectrometry to determine the contents of Cr and Mn in the cementite. The total value thereof was obtained as the total content {Cr+Mn} of Cr and Mn in the cementite in % by mass.
The total content of Cr and Mn in the steel in % by mass was measured as follows. A specimen of about 4 g was taken from the above-mentioned sample and dissolved in an acid solution, followed by analysis using the ICP optical emission spectrometry, whereby the Cr content and Mn content of the steel were determined to obtain the total value thereof [Cr+Mn]. The total content {Cr+Mn} of Cr and Mn in the cementite in % by mass was divided by the total amount of [Cr+Mn] of Cr and Mn in the steel in % by mass, thereby determining the concentration ratio {Cr+Mn}/[Cr+Mn].
To evaluate the cold-workability, the hardness of each sample obtained after the spheroidizing annealing was measured as follows. The Vickers hardness test was conducted on a test piece in accordance with JIS Z2244 (2009) at the D/4 position (D: diameter of the steel wire) of the test piece. The Vickers hardness obtained by calculating the average hardness at three or more points on the sample was defined as the hardness after the spheroidizing annealing. The measurement results are shown in Table 3. In Table 3, “spheroidizing hardness” is defined as the hardness after the spheroidizing annealing. In the present example, when the C content (% by mass), Cr content (% by mass), and Mo content (% by mass) of the steel are expressed as [C], [Cr], and [Mo], respectively (elements not included are assumed to be zero % by mass), the steel was evaluated as “OK” because of excellent cold-workability in a case where its hardness after the spheroidizing annealing satisfied the equation (2) below, whereas the steel was evaluated as “NG” because of inferior cold-workability in a case where its hardness after the spheroidizing annealing did not satisfy the equation (2) below.
Hardness (HV) after the spheroidizing annealing<91 ([C]+[Cr]/9+[Mo]/2)+91 (2)
To evaluate the hardenability, the hardness of each sample obtained after the quenching process was measured as follows. First, in order to perform sufficient hardening in the quenching process, each sample obtained after the spheroidizing annealing was processed to have a thickness (t) of 5 mm, which was the length in the rolling direction, and it was then prepared as a specimen for quenching treatment. The specimen was held at a high temperature of A3+(30 to 50° C.) for 5 minutes in the quenching process, and was then water-cooled after the high temperature was held. The A3 is a value derived from the following equation (5). The high-temperature holding time here was defined as the time that elapses after the furnace temperature reached the set temperature.
A3 (° C)=910−203×√([C])−14.2×[Ni]+44.7×[Si]+104×[V]+31.5×[Mo]+13.1×[W]−30×[Mn]−11×[Cr]−20×[Cu]+700×[P]+400×[Al]+120×[As]+400×[Ti] (5)
where an expression [element] represents the content of each element (% by mass), and the content of an element not included is calculated as 0%.
The Vickers hardness test was conducted on the specimen, obtained after the quenching process, at a t/2 and D/4 position (D: diameter of the steel wire, t: thickness of the sample) of the specimen. The Vickers hardness obtained by calculating an average value of the hardnesses at three or more points on the specimen was defined as the hardness after the quenching process. The measurement results are shown in Table 3. In Table 3, the hardness after the quenching process was referred to as the “quenching hardness”. In the present example, when the C content (% by mass) of the steel is expressed as [C], the steel was evaluated as “OK” because of excellent hardenability in a case where its hardness after the quenching process satisfied the equation (3) below, whereas the steel was evaluated as “NG” because of inferior hardenability in a case where its hardness after the quenching process did not satisfy the equation (3) below.
Hardness (HV) after the quenching process>380 In ([C])+1010 (3)
In Table 3, when both the hardness after the spheroidizing annealing and the hardness after the quenching process were OK, the overall judgment was made “OK” because the steel had both excellent cold-workability and excellent hardenability. When at least one of the hardness after the spheroidizing annealing and the hardness after the quenching process was NG, the overall judgment was made “NG” because the steel could not achieve both excellent cold-workability and excellent hardenability. In Tables 2 and 3, underlined values indicate that they deviated from the specified range of the present disclosure or did not meet the desired properties.
710
30
11
1
730
730
0
0
0
H1
0.232
146
NG
NG
H2
0.645
136
NG
NG
I
0.906
0.262
706
NG
NG
J
0.696
0.263
144
NG
NG
K
0.256
133
NG
NG
L
1.028
0.213
693
NG
NG
M
0.577
140
NG
NG
N
0.702
0.111
134
NG
NG
O
0.708
135
NG
NG
P
0.585
0.193
143
NG
NG
H1
1.110
0.140
129
NG
NG
H1
1.130
0.104
106
NG
NG
T
1.100
125
NG
NG
V
1.160
124
NG
NG
U
1.120
133
NG
NG
V
1.120
134
NG
NG
The results in the table will be discussed. The following No. refers to sample No. in Table 3. Nos. 1 to 11 are inventive examples satisfying all of the composition, metallurgical microstructure, and spheroidizing annealing conditions specified by the embodiment of the present invention.
In Nos. 12, 20, 22, and 23, since the number of times of the cooling-heating process was insufficient, the total content of Cr and Mn in the cementite was low, or the coarsening of cementite was insufficient, resulting in higher hardness after the spheroidizing annealing than the reference value and inferior cold-workability.
No. 13 was an example of performing annealing after wire drawing at an area reduction ratio of 25%, and this wire drawing could increase the total content of Cr and Mn in the cementite. However, no cooling-heating process was performed, and thus the average size of all the cementite could not be at a certain level or more, resulting in higher hardness after the spheroidizing annealing than the reference value and inferior cold-workability.
No. 14 is an example where annealing was performed under the annealing condition SA2 of Patent Document 3 as the manufacturing condition I that satisfied the manufacturing conditions shown in Patent Document 3. Under this manufacturing condition, the annealing excessively coarsens cementite, making the hardness after the quenching process lower than the reference value, resulting in inferior hardenability.
In No. 15, since the temperature T2 was set to 710° C., which was higher than A1−17° C, the coarsening of cementite during the cooling from the temperature T1 became insufficient, and the total content of Cr and Mn in the cementite was low, resulting in higher hardness after the spheroidizing annealing than the reference value and inferior cold-workability.
In Nos. 16 and 17, since the average temperature increase rate R from the temperature T2 was low, the total content of Cr and Mn in the cementite became low, and the hardness after the spheroidizing annealing was not less than the reference value, resulting in inferior cold-workability or in lower hardness after the quenching process than the reference value, leading to inferior hardenability.
No. 18 is an example where annealing was performed under the manufacturing condition M, which satisfied the manufacturing condition mentioned in Patent Document 1. Under this manufacturing condition, the heat holding time was 0.5 hour especially at the temperature T1, which was short. Thus, a large amount of bar-shaped cementite of a small size remained in crystal grains, resulting in the average size of all the cementite being not larger than or equal to the certain level, higher hardness after the spheroidizing annealing than the reference value, and inferior cold-workability.
No. 19 is an example where annealing was performed under the conditions c of Patent Document 2, as the manufacturing condition N that satisfied the manufacturing conditions shown in Patent Document 2. Under this manufacturing condition, holding of the temperature at T1 was not performed, or the like. Thus, a large amount of bar-shaped cementite of a small size remained in crystal grains, resulting in the average size of all the cementite being not larger than or equal to the certain level. Because of low average temperature increase rate R from the temperature T2, the total content of Cr and Mn in the cementite became low, resulting in the hardness after the spheroidizing annealing being not less than the reference value and inferior cold-workability.
In No. 21, since the temperature T3 was 730° C. and lower than (A1+8° C.), the total content of Cr and Mn in the cementite became low, resulting in the hardness after the spheroidizing annealing being not less than the reference value and inferior cold-workability.
In Nos. 24 to 27, since no cooling-heating process was performed, or the cooling-heating process was not repeated, the coarsening of cementite became insufficient, resulting in the average size of all the cementite being not larger than or equal to the certain level, the hardness after the spheroidizing annealing being not less than the reference value, and inferior cold-workability.
The present application claims priority to Japanese Patent Application No. 2021-061575 and Japanese Patent Application No. 2021-211501, the disclosures of which are incorporated herein by reference in its entirety.
The steel wire for machine structural parts according to the present embodiment exhibited excellent cold-workability, such as low deformation resistance at room temperature when manufacturing various machine structural parts, the ability to suppress wear and fracture of plastic working jigs such as dies, and the ability to suppress cracking during heading, for example. Further, the steel wire can also ensure high hardness by means of the quenching process after the cold-working because of its excellent hardenability. For these reasons, the steel wire for machine structural parts according to the present embodiment is useful as a steel wire for cold-working machine structural parts. For example, the steel wire for machine structural parts according to the present embodiment can be used to manufacture various machine structural parts, such as automobile parts and construction machinery parts, by performing cold working such as cold forging, cold heading, and cold rolling. Specific examples of such machine structural parts, electrical parts and the like, which include machinery parts, such as bolts, screws, nuts, sockets, ball joints, inner tubes, torsion bars, clutch cases, cages, housings, hubs, covers, cases, bearing washers, tappets, saddles, bulgs, inner cases, clutches, sleeves, outer races, sprockets, cores, stators, anvils, spiders, rocker arms, bodies, flanges, drums, joints, connectors, pulleys, fittings, yokes, mouthpieces, valve lifters, spark plugs, pinion gears, steering shafts, and common rails.
| Number | Date | Country | Kind |
|---|---|---|---|
| 2021-061575 | Mar 2021 | JP | national |
| 2021-211501 | Dec 2021 | JP | national |
| Filing Document | Filing Date | Country | Kind |
|---|---|---|---|
| PCT/JP2022/013281 | 3/22/2022 | WO |
