JP2008189985A - Hot rolled steel sheet having local ductile performance, and method for producing the same - Google Patents

Abstract

<P>PROBLEM TO BE SOLVED: To provide a hot rolled steel sheet having excellent local ductile performance, and to provide a method for producing the same. <P>SOLUTION: The hot rolled steel sheet having excellent local ductile performance comprises one or more kinds selected from Ti, Nb, Mo and V of ≤0.05% in total, and contains ferrite as a main phase, and in which, the average crystal grain diameter D (μm) of the ferrite in the depth position of the 1/4 of the sheet thickness from the steel sheet surface satisfies the following inequalities (1) and (2), a yield ratio satisfies≥0.8, and the average plastic tangent gradient H' in the strain range from a plastic strain of 0.005 after a yield to a strain of 65% of uniform elongation in a tensile test satisfies the following inequality (3). The inequality (1) is 1.2≤D≤7, the inequality (2) is D≤2.7+5000/(5+350*C+40*Mn)<SP>2</SP>, and the inequality (3) is 0.1≤H'/TS≤-2×YR+3.1, wherein C and Mn denote the contents (unit: mass%) of the respective elements in steel, TS denotes tensile strength (MPa), and YR denotes a yield ratio. <P>COPYRIGHT: (C)2008,JPO&INPIT

Description

  The present invention relates to a hot-rolled steel sheet having excellent impact absorbability and shape freezing properties and excellent local elongation performance, and a method for producing the same. Specifically, the present invention relates to a hot-rolled steel sheet suitable for materials used for automobiles, home appliances, machine structures, buildings, etc., excellent in shock absorption and shape freezing properties, and excellent in local ductility, and a method for producing the same. .

  In recent years, it has been important to improve the shock absorption characteristics of steel sheets used as materials for structural parts of automobiles and other transportation machines and various industrial machines from the viewpoint of improving safety during collisions. .

  In order to increase the yield strength of the steel sheet in order to improve the impact absorbing performance, it is effective to refine the structure of the steel sheet. Therefore, many methods for refining the structure of the steel sheet have been proposed.

  The means for refining the structure in the prior art are summarized as follows: (i) large rolling reduction method, (ii) controlled rolling method, (iii) alloy element addition method, or a combination thereof.

  (I) The large rolling reduction method increases the rolling reduction to about 50% or more, accumulates large strain by one-pass rolling, and then transforms from austenite to fine ferrite, or uses large strain. This is a technique for recrystallizing relatively coarse ferrite into fine ferrite. According to such a method, after heating to a temperature of about 1000 ° C. or lower and then rolling under a large pressure in a low temperature region of about 700 ° C., an ultrafine ferrite structure of 1 to 3 μm can be obtained.

(Ii) The controlled rolling method is generally a method of cooling after performing multi-pass rolling at a temperature of about 800 ° C. or higher and a rolling reduction per rolling of 20 to 40% or less. There are many methods such as a method in which the rolling temperature is set to a narrow temperature range near the Ar ₃ point, a method of shortening the time between rolling passes, and a method of dynamically recrystallizing austenite by controlling the strain rate and temperature. It is disclosed.

  (Iii) The alloy element addition method promotes refinement of ferrite crystal grains by adding a small amount of an alloy element that suppresses recrystallization and recovery of austenite. Alloy elements such as Nb and Ti form carbides or segregate at grain boundaries to suppress austenite recovery and recrystallization, so that austenite grains after hot rolling are refined, The ferrite crystal grains obtained by transformation are also refined.

  The alloy element addition method (iii) is often used in combination with the above-described large rolling method (i) or the controlled rolling method (ii). The alloy element addition method (iii) has a certain effect of suppressing the ferrite grain growth even during the heat treatment.

There is Patent Document 1 as a prior art document that refers to these (i) large rolling rolling methods, (ii) controlled rolling methods, and (iii) methods of adding alloy elements. Here, processing with a total rolling reduction of 50% or more is performed once or twice within one second in a temperature range of Ar ₁ + 50 ° C. to Ar ₃ + 100 ° C., and in a temperature range of 600 ° C. or more after completion of processing. A method of performing forced cooling at a cooling rate of 20 ° C./second or more is disclosed.

  Patent Document 2 discloses that the first stand entry side and the last stand where the reduction in the dynamic recrystallization temperature range is performed in a reduction pass of five or more stands and the reduction is applied in the dynamic recrystallization temperature range. A method of setting the temperature difference on the outlet side to 60 ° C. or less is disclosed.

  Thus, if only the impact absorption characteristic represented by the yield strength value of a steel plate is taken into consideration, a high yield strength steel plate having a good impact absorption capability is provided by various methods.

  On the other hand, when a steel plate is press-molded, shape defects are likely to occur. In particular, steel with high yield strength with good shock absorption ability has poor shape freezing properties, and shape defects tend to occur during press molding, so there is a problem that it cannot be applied to members that require accuracy. .

  The defective shape of the steel plate at the time of press molding is caused by a spring back generated when the material is bent. It is known that the amount of springback is correlated with the bending portion reaching stress.

  FIG. 1 shows the ultimate stress at the bending portion when a bending test is performed on two types of materials A and B. Here, it is known that the material A has a large ultimate stress but has a large amount of springback, and the material B has a small amount of springback because the ultimate stress is small. It is known that the ultimate stress value has a positive correlation with the yield strength YS, and further has a positive correlation with the tensile strength TS. Therefore, in order to reduce the springback amount and improve the shape freezing property, the yield strength YS and / or the tensile strength TS of the material may be reduced. When the tensile strength TS is the same, the yield ratio YR is set. What is necessary is just to reduce.

  A technique for improving the shape accuracy of a steel sheet with poor shape freezing properties is disclosed in Patent Document 3, in which reverse bending is applied to the bent portion in advance so that the stress distribution generated in the thickness direction at the time of bending is balanced. A technique for suppressing the springback by applying is disclosed.

  Patent Document 4 discloses a technique for improving the shape freezing property by controlling the Rankford value and texture of a steel plate.

JP 59-205447 A Japanese Patent Laid-Open No. 11-152544 JP-A-7-148527 JP 2001-303175 A

  As described above, (i) large rolling reduction method, (ii) controlled rolling method, and (iii) alloy element addition method are known as means for refining the structure.

  However, (i) the large reduction rolling method is not only industrially difficult to implement, but the fine ferrite structure tends to grow by heat treatment. Therefore, after passing through the welding process or the hot dipping process, the desired mechanical characteristics are lost, and sufficient shock absorbing characteristics cannot be obtained in actual parts.

  (Ii) Although the controlled rolling method is said to be water-cooled immediately after rolling, cooling immediately after the rolling starts 0.2 seconds or more after the rolling, and the cooling rate is at most 250 ° C./second. Degree. In such a method, the ferrite crystal grain size of a low-carbon steel having a simple composition is only about 5 μm. Therefore, it is not possible to sufficiently improve the shock absorption characteristics.

  (Iii) Although the alloy element addition method reduces the ferrite crystal grain size, it lowers the volume fraction of ferrite. Further, the raw material cost increases by the amount of the alloy element to be added.

  Thus, according to (i) large rolling reduction method, (ii) controlled rolling method, or (iii) alloy element addition method disclosed in Patent Documents 1 and 2, the high yield steel plate having a fine crystal structure. However, the thermal stability of the tissue is low.

  Therefore, when a steel plate is pressed and assembled by welding or the like to obtain parts, or when hot-plating is applied to the steel plate, the crystal grains are likely to be coarsened by the heat applied during welding or the heat applied during the hot-dipping process. May be damaged. For example, when the crystal structure near the HAZ (Heat Affected Zone) is coarsened and softens during welding, stress concentration is likely to occur in this area. The result is that the characteristics cannot be obtained.

  In addition, when the (iii) alloy element addition method is used in combination with the above-described large rolling method (i) or the controlled rolling method (ii), there is an effect of suppressing the ferrite grain growth even during heat treatment. However, since it is insufficient to suppress the grain growth in the welding process or hot dipping process of ultrafine ferrite crystal grains, applicable steel types are limited.

  However, even if the yield strength of the steel sheet is increased by refining the structure in order to improve the impact absorbing performance of the steel sheet, it is inferior to the local elongation performance. It tends to occur, and cracks are likely to occur at buckled wrinkles especially during impact absorption.

  FIG. 2 is a diagram illustrating a state in which a crack is generated in a bent portion when a steel plate is bent. When local ductility is poor, cracking occurs outside the bend.

  In addition, conventional steel having high yield strength has poor shape freezing properties, and shape defects are likely to occur during press molding, and therefore cannot be applied to members that require accuracy. In particular, in the case of close contact bending (hem processing), the bent portion often does not have a sharp shape because of poor local elongation performance.

  FIG. 3 is an example of the shape of a bent portion when a steel plate is subjected to close contact bending. (a) is a good example, and (b) is a bad example. When the local ductility is excellent, the bent part has a sharp shape as shown in (a).

  As described above, in order to improve the shape freezeability, the springback amount may be reduced by reducing the yield strength YS (yield ratio YR when the tensile strength TS is the same) and the tensile strength TS of the material. However, a material with low yield strength YS (yield ratio YR when tensile strength TS is the same) and tensile strength TS is inferior in impact absorption performance and fatigue strength characteristics. That is, it has been difficult to achieve both the impact absorbability and the shape freezing property of the hot-rolled steel sheet.

  As described above, an improvement proposal has been made on the shape freezing property. However, in the method of improving the shape freezing property disclosed in Patent Document 3, a pre-processing treatment trace remains in the bent portion to impair the appearance, and it is necessary to perform the bending process in two steps, resulting in an increase in cost. Moreover, the local extension performance is not improved.

  Moreover, in the method of improving the shape freezing property disclosed in Patent Document 4, the yield strength ratio of the steel sheet obtained thereby is low, and sufficient impact absorption characteristics cannot be obtained. Moreover, the local extension performance is not improved.

  Furthermore, when assembling the steel plate by welding after pressing and obtaining parts or hot-plating the steel plate, even if the structure of the steel plate is refined and mechanical properties such as shock absorption properties are improved, Due to the heat applied to the steel plate during welding or hot dipping, the crystal grains are likely to be coarsened and the mechanical properties thereof are likely to be impaired.

  As described above, a steel sheet having both impact absorption characteristics and shape accuracy while maintaining the surface properties has not been realized. In addition, a steel plate that is thermally stable while achieving both shock absorption characteristics and shape accuracy has not been realized. Furthermore, it is inferior in local extended performance.

  FIG. 4 is a plot of various hot-rolled steel sheets having the same tensile strength TS by their yield ratio YR and springback amount. As described above, when the tensile strength TS is the same in the conventional material, the yield ratio YR and the springback amount have a positive correlation. Therefore, when obtaining a small springback amount, the yield ratio YR is also It turns out that it becomes small. Such a hot-rolled steel sheet cannot achieve both impact absorption and shape freezing properties, and is inferior in local rolling performance.

  The aim of the material of the present invention is to have both a small springback amount and a large yield ratio YR, as well as excellent local elongation performance, in order to achieve both shock absorption and shape freezing without impairing the mechanical properties of the steel sheet. It is to provide a rolled steel sheet. Another aim of the material of the present invention is to achieve both the shock absorption characteristics and the shape accuracy, and to obtain parts by assembling the steel sheet with excellent local elongation performance by welding after pressing, or when hot-plating the steel sheet However, it is to provide a hot-rolled steel sheet that is thermally stable.

  The present invention has ultrafine crystal grains, has a high yield strength with a yield strength to yield strength ratio (yield ratio YR) of 0.8 or more, has excellent shock absorption characteristics and shape freezing properties, and is locally A first object is to provide a hot-rolled steel sheet having excellent ductility and a method for producing the same.

  Furthermore, the present invention has ultra-fine crystal grains, has a high yield strength with a yield strength to yield strength ratio (yield ratio YR) of 0.8 or more, and has excellent shock absorption characteristics and shape freezing properties. In addition, a second object is to provide a hot-rolled steel sheet having excellent local rolling performance and having thermal stability capable of withstanding the heat of the welding process and the hot dipping process, and a method of manufacturing the same.

  The inventors of the present invention have a high yield strength with respect to a hot-rolled steel sheet having a fine ferrite grain structure, and at the same time provide both impact absorption characteristics and shape freezing properties, and further impart local elongation performance. Various studies and experiments were conducted. Furthermore, various examinations and experiments were conducted in order to provide a hot-rolled steel sheet having thermal stability that can withstand the heat of the welding process and the hot dipping process. As a result, the following findings (a) to (j) were obtained.

(a) About keeping the average crystal grain size of ferrite within a certain range Since the strength increases as the crystal grain size of ferrite decreases, the shock absorption characteristics can be improved accordingly, but the crystal grain size becomes too small It was found that the grain growth driving force by the grain boundary energy increases, so that the grain growth is promoted during hot rolling.

Specifically, if the average crystal grain size of ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface is less than 1.2 μm, it becomes difficult to suppress grain growth during hot rolling. On the contrary, if the average crystal grain size of ferrite exceeds 2.7 + 5000 / (5 + 350 · C + 40 · Mn) ² μm or 7 μm, the improvement in mechanical properties due to miniaturization cannot be sufficiently expected. found.

Therefore, in order to obtain a hot-rolled steel sheet having excellent mechanical properties with excellent shock absorption characteristics, 1.2 μm is adopted as the lower limit of the average crystal grain size of ferrite, and 2.7 + 5000 / (5 + 350 · C + 40) as the upper limit. -Mn) It is necessary to adopt the smaller value of ² μm and 7 μm.

  Therefore, the average crystal grain size D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel plate surface needs to satisfy the following formulas (1) and (2).

1.2 ≦ D ≦ 7 (1) Formula D ≦ 2.7 + 5000 / (5 + 350 · C + 40 · Mn) ² Equation (2) where D is the average crystal grain size (μm) of ferrite at a depth of 1/4 of the plate thickness from the steel sheet surface, and C and Mn are the contents (mass of each element in the steel) %).

(b) Making the yield ratio (YR) 0.8 or more High impact absorbing materials have a high yield ratio YR value when compared with the same tensile strength TS, and their mechanical properties have a high yield strength YS. Therefore, the plastic work increases due to deformation at the time of impact absorption. Therefore, in order to obtain sufficient collision absorption performance, the yield ratio YR needs to be 0.8 or more. The yield ratio YR is preferably 0.85 or more.

(c) Regarding the upper and lower limits of the average plastic tangent gradient H ′ in the range from the plastic strain after yielding 0.005 to the 65% strain of uniform elongation in the JIS No. 5 tensile test, the present inventors Springback in bending forming is based on the idea that if the strain generated when bending deformation is applied to a hot-rolled steel sheet can be localized, a hot-rolled steel sheet with excellent shape freezing properties can be obtained. As a result of various studies on the method for reducing the following, the following knowledge was obtained.

  FIG. 5 shows a cross-sectional view around a bent portion of a hot-rolled steel sheet in right-angle bending. The size of the springback in this bending process is as follows: (i) Distribution of difference in thickness direction of residual stress in bending direction (difference between residual stress inside bending and residual stress outside bending), and (ii) Residual stress inside and outside bending It is determined by the distribution in the bending direction of the region where the difference occurs.

  Therefore, if the residual stress and the bending direction in bending can be controlled, the springback can be reduced.

  Residual stress changes depending on the behavior of bending deformation during bending, but the difference in residual stress inside and outside the bend in (i) correlates with the above-mentioned stress at the bending part when bending the material. It is known that In addition, since the material with low work hardening characteristics has a narrow deformation region, the strain is likely to be localized, and the region where the residual stress difference between the inside and outside of the bending (ii) occurs can be localized. Can be reduced.

  Next, the plastic tangential gradient is a tangential gradient of a stress-plastic strain curve in a tensile test, and is one value indicating the propagation of strain during material deformation together with a work hardening index. In particular, the average plastic tangent gradient H ′ in the range from the plastic strain after yielding 0.005 to the strain of 65% of uniform elongation in the JIS No. 5 tensile test is suitable as an index, and the average plastic tangential gradient H ′ in bending deformation is suitable. If it is low, the shape freezeability is improved because the strain is localized.

  FIG. 6 is a plastic tangent gradient curve, in which the X axis indicates plastic strain (true strain) and the Y axis indicates stress (true stress). The average plastic tangent gradient H ′ is an average value of the tangential gradient within the range from the plastic strain after yielding 0.005 to the 65% strain of uniform elongation.

  FIG. 7 is an enlarged view of the above-mentioned limited range of the plastic tangent gradient curve of FIG. 6. Here, the true strain value of the X-axis of the limited range is divided into 10 equal parts (H′1, H′2, H′3,..., H′10), and the average value of the plastic tangent gradient in each section is obtained, indicating that the average plastic tangent gradient H ′ can be obtained. Here, the average plastic tangent gradient H ′ is obtained by dividing the true strain value of the X-axis of the limited range into 10 equal parts, but it is not particularly important to divide the limited range into 10 equal parts. For example, it may be obtained by dividing into 20 equal parts. Or you may obtain | require by linear approximation.

  FIG. 8 is a plot of data obtained from examples described later, with YR on the X axis and H ′ / TS on the Y axis. ○ is excellent in both shock absorption and shape freezing, and ■ is inferior to at least one of shock absorption and shape freezing.

  As can be seen from FIG. 8, when H ′ / TS exceeds the value of [−2 × YR + 3.1], distortion localization is difficult to occur, and a sufficient springback reduction effect cannot be obtained. Further, from the viewpoint of shock absorption, since a certain degree of work hardening property is required for the material, a material that is not work hard at all is inappropriate in terms of shock absorption. Therefore, the lower limit of H ′ / TS needs to be 0.1. A preferred lower limit is 0.13.

  Here, the characteristic value H ′ / TS is used for the following reason. As described above, the amount of springback increases in correlation with the average plastic tangent gradient H ′ and the tensile strength TS, and the value of the average plastic tangential gradient H ′ also increases in correlation with the tensile strength TS. This is to make it possible to compare the amount of springback even in different steel plates.

  Therefore, the average plastic tangential gradient H ′ in the range from the plastic strain after yielding 0.005 to the 65% strain of uniform elongation in the JIS No. 5 tensile test needs to satisfy the following formula (3).

0.1 ≦ H ′ / TS ≦ −2 × YR + 3.1 (3) where H ′ is one from the plastic strain after yielding 0.005 in the tensile test. The mean plastic tangent gradient in the range up to 65% strain of uniform elongation, TS is the tensile strength (MPa), and YR is the yield ratio.

  The reason why the lower limit of the range of adoption of the average plastic tangent gradient H ′ is defined as “plastic strain 0.005” after yielding is as follows.

  The bending process is usually performed in a region where the plastic strain of the plate thickness surface layer portion is 0.005 or more. This is because in a region where the plastic strain is less than 0.005, for example, when the plate thickness is 2 mm, the plastic strain at a position of 0.5 mm from the surface layer portion toward the inside of the plate thickness is an extremely low strain of 0.0025 or less. This is because sufficient processing is not performed. Therefore, in the region where the plastic strain is less than 0.005, the effect of reducing the spring back due to the localization of the strain intended by the present invention is not sufficiently exhibited. Therefore, the lower limit of the range of adoption of the average plastic tangent gradient is defined as “plastic strain 0.005” after yielding.

  Moreover, the reason for prescribing the upper limit of the adoption range of the average plastic tangent gradient H ′ as “up to a strain of 65% of uniform elongation” is as follows.

  In bending, the plastic strain of the bent portion is often processed within a range of 65% or less of the uniform elongation. For example, in a hot rolled steel sheet having a bending radius R = 10 mm and a sheet thickness of 1.4 mm, which is a general condition, the plastic strain generated on the outermost layer surface of the bending portion is 0.073. Here, when the uniform elongation (UEl) of a general material is 0.15, the strain (ε) of 65% of the uniform elongation (UEL) is 0.097. Therefore, the upper limit of the adoption range of the average plastic tangent gradient H ′ is set to “up to 65% strain of uniform elongation”.

(d) About defining the upper limit of the content of Ti, Nb, V and Mo As a means for increasing the yield strength of steel, it is effective to contain precipitation strengthening elements such as Ti, Nb, V, and Mo. It has been known. This is because these elements form fine carbonitrides in steel and inhibit dislocation movement. Up to now, these precipitation strengthening elements have been actively used for imparting a high yield ratio to a practical structural hot-rolled steel sheet. Therefore, also in the present invention, detailed examination was performed on the influence of the contents of Ti, Nb, V and Mo on the yield strength and shape freezing property.

  As a result, the yield ratio increases as the total content of Ti, Nb, V, and Mo increases. On the other hand, when compared at the same yield ratio, the Ti, Nb, V, and Mo are not contained. Compared with fine-grained steel and ultrafine-grained steel with a small total content of Ti, Nb, V, and Mo, a result of inferior springback characteristics was obtained.

  The reason for this is not clear, but is presumed as follows.

  In the high yield ultrafine grain steel according to the present invention which does not contain Ti, Nb, V and Mo, or contains a small amount thereof, relatively soft and isotropic ferrite grains are present finely and relatively uniformly. Therefore, it is considered that local yield region units at the time of processing are finely and finely dispersed.

  On the other hand, high yield steel sheets containing a certain amount of Ti, Nb, V or Mo are likely to form pseudopolygonal ferrite with complex meandering of ferrite grain boundaries, and between grains due to the fine precipitation strengthening amount (hardness). Because relatively large variations are likely to occur, local yield region units are not evenly dispersed during processing, yield point elongation is reduced, plastic tangent gradient is increased, and strain is difficult to localize, resulting in poor shape freezeability. Conceivable.

  Needless to say, the uniform dispersion of local yield region units, which is considered to be effective for improving the shape freezing property, depends on the particle size, and fine particles are more advantageous.

  Therefore, 0.05% or less of Ti, Nb, Mo and V in total is 0.05% or less in total in order to obtain a good shape with no correction or slight correction within the practical range. It is necessary to make it content of. In addition, it is preferable to set it as 0.03 or less content. It is more preferable that the impurity level is not mixed but added.

  The carbon steel or low alloy steel used in the present invention preferably contains C: 0.01 to 0.25%, and further Si, Mn, Al, P, Ti, Nb, V, Cr, Cu , Mo, Ni, Ca, REM, or B may be included.

(e) About local extending | stretching performance FIG. 9: shows sectional drawing of the bending part periphery of a hot-rolled steel plate in close_contact | adherence bending processing (hem processing). Even in the close contact bending process, the size of the spring back is determined by the distribution of (i) the difference in the thickness direction of the residual stress in the local bending direction (the difference between the residual stress inside the local bend and the residual stress outside the local bend), and (ii It is determined by the distribution in the local bending direction of the region where the difference in residual stress between the inside and outside of the local bending occurs.

  Therefore, if the residual stress and the local bending direction in the tight bending process can be controlled, the springback can be reduced as in the case of the right angle bending.

  Residual stress varies depending on the behavior of local bending deformation during close contact bending, but as with right angle bending, the difference in residual stress inside and outside the local bending in (i) is the same as when the material is subjected to local bending. It is known that there is a correlation with the local bending part ultimate stress. In addition, since the material with low work hardening characteristics has a narrow deformation region, the strain is likely to be localized, and the region where the local bending internal / external residual stress difference (ii) occurs can be localized. The amount can be reduced.

  The local elongation performance refers to the elongation performance in a state in which constriction occurs after the maximum load is generated in the JIS No. 5 tensile test. Therefore, excellent local extension performance means that in close-contact bending, the occurrence of cracks on the outside of the bend is suppressed and the bent part becomes sharp, and the sharp shape remains after processing because the spring back amount is low. It means having a shape freezing property of being maintained.

  In order to obtain excellent local elongation performance, the present inventors have conducted various studies and experiments. As a result, the average plastic tangential gradient H ′ and the crystal grain size of the steel sheet correlate with this local elongation performance. It has been found that That is, in the case of the low H ′ material, when the steel plate is bent, the strain concentrates in a narrow range of the local bending portion, thereby reducing the amount of springback and the fine grain size of the steel plate. Since it is uniform, generation | occurrence | production of the crack of a local bending part is suppressed, and it is thought that a local bending part becomes a sharp shape.

(f) The average crystal grain diameter D _s (μm) of ferrite on the steel sheet surface layer is within a certain range with respect to the average crystal grain diameter D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface. Furthermore, in order to make the local ductility excellent, the average crystal grain diameter D _s (μm) of the ferrite on the steel sheet surface layer is set to the average of the ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface. It is preferable to stay within a certain range with respect to the crystal grain size D (μm). In order to further suppress the occurrence of cracks in the local bending portion, it can be achieved by making the average crystal grain size of ferrite on the surface of the steel sheet finer than the average crystal grain size of ferrite inside the steel sheet.

That is, the average crystal grain diameter D _s (μm) of ferrite on the steel sheet surface layer and the average crystal grain diameter D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface are expressed by the following formula (4): Is preferably satisfied.

D _s /D≦0.8 (4) where D _s is the average crystal grain size (μm) of ferrite on the steel sheet surface layer, and D represents the average crystal grain size (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel plate surface.

(g) About keeping the crystal grain size distribution of ferrite within a certain range In order to further improve the thermal stability of the steel sheet, it is preferable to keep the distribution of ferrite crystal grain size within a certain range. One factor that causes grain growth at high temperatures is the driving force based on the energy of the grain boundaries.If relatively large ferrite crystal grains are mixed in a fine ferrite structure, the large ferrite crystal grains As a driving force, it easily integrates with the surrounding fine ferrite crystal grains, and the grain growth proceeds rapidly. Therefore, in order to suppress the growth rate of ferrite crystal grains at high temperature, the ferrite crystal grains are refined and the average crystal grain size D (μm) satisfies the above formulas (1) and (2). In addition to the fixed range, the ferrite at the depth position of ¼ of the plate thickness from the steel plate surface is 80% or more of the ferrite crystal grains in terms of area ratio of the average crystal grain size D (μm). It is preferable that the particle size distribution be within a range of 1/3 to 3 times. That is, it is preferable that the area ratio of the crystal grains whose crystal grain size d (μm) satisfies the following formula (5) is 80% or more.
D / 3 ≦ d ≦ 3D (5) where d is the ferrite crystal grain size (μm) and D is the surface of the steel plate. The average crystal grain size (μm) of ferrite at a depth position of ¼ of the thickness is shown.

  More preferably, the grain size distribution is such that 90% or more of ferrite crystal grains fall within the range of 1/3 to 3 times the average crystal grain size D (μm).

(h) A _On the upper limit of the product D · X of the average grain size D of ferrite and the average grain size D of ferrite at a temperature near 700 ° C just below _one point The grain growth rate of ferrite grains at high temperatures is Increases with increasing temperature. In general, the temperature range in which the problem of ferrite grain growth occurs in the welding process or hot dipping process is the temperature range immediately below A ₁ point (near 730 ° C.) to near A ₃ point, and ferrite grain growth occurs in this temperature range. Speed varies greatly. However, as shown in the above (a), the average crystal grain size D of ferrite (D) at a depth position of ¼ of the plate thickness from the steel sheet surface, that is, the steel sheet in which the average crystal grain size of ferrite is within a specific range. Since it was found that the temperature characteristics of the grain growth rate of the steel sheet in which μm) satisfies both the formulas (1) and (2) are determined by the grain growth rate of ferrite at a temperature near 700 ° C., 700 ° C. The upper limit is the grain growth rate of ferrite at a nearby temperature, that is, the product D · X (μm ² / min) of the average crystal grain size increase rate X (μm / min) and the average crystal grain size D (μm). It was found that no problem occurs even when heated to a higher temperature in the welding process or hot dipping process. As a result of the experiment, it was also found that the product D · X needs to be set to 0.1 μm ² / min or less. Incidentally, the product D · X is preferably from 0.07 .mu.m ² / min, more preferably 0.05 .mu.m ² / min or less.

  Therefore, when heated to a higher temperature in the welding process or the hot dipping process, the rate of increase in the average crystal grain diameter D (μm) of ferrite at 700 ° C. at a depth position of ¼ of the sheet thickness from the steel sheet surface. It is preferable that X (μm / min) and the average crystal grain size D (μm) satisfy the following formula (6).

Here D · X ≦ 0.1 ················ (6) formula, D is the average from the steel sheet surface of the ferrite in the 1/4 depth position of the sheet thickness crystal The particle size (μm) and X represents the rate of increase (μm / min) at 700 ° C. of the average crystal particle size D (μm) of the ferrite.

In order to further reduce the grain growth rate, the dislocation density in the ferrite crystal grains is preferably 10 ⁹ / cm ² or less, more preferably 10 ⁸ / cm ² or less.

(i) To moderate the change in crystal grain size in the plate thickness direction The gradual change in crystal grain size in the plate thickness direction contributes to the improvement of the mechanical properties of the steel sheet. For example, since it is finer on the plate surface side, local bendability in which the vicinity of the steel plate surface is greatly deformed is improved. In addition, the propagation of cracks generated from the vicinity of the surface can be effectively suppressed by the finer surface structure, so that fatigue characteristics are also improved.

Therefore, the crystal grain size d _s (μm) at a depth position of 100 μm from the steel plate surface, the crystal grain size d (μm) at a depth position of ¼ of the plate thickness from the steel plate surface, and the crystal grains at the center portion of the plate thickness The diameter d _c (μm) preferably satisfies the following expressions (7) and (8).

_{d s ≦ 0.7d c ················ (7} ) formula d ≦ 0.9d _c ················ ( 8) where d _s is the crystal grain size (μm) at a depth of 100 μm from the steel sheet surface, d is the crystal grain size (μm) at a depth position of ¼ of the plate thickness from the steel sheet surface, Then, d _c denotes the crystal grain size in the central portion of the thickness ([mu] m).

Incidentally, the causes have grain diameter change of the thickness of the plate that satisfies _{d s} ≦ 0.6d _c and d ≦ 0.85d _c, more preferably.

(j) A method for producing a hot-rolled steel sheet having shock absorption characteristics and shape freezing property, or thermal stability that can withstand the heat of a welding process or a hot dipping process and having excellent local elongation performance By adopting rolling in a high temperature region, it is possible to provide an industrial method that is easy to roll and has high productivity.

First, multi-pass hot rolling is started from the austenite temperature range, and the final rolling pass is finished at a high temperature of Ar ₃ points or higher and 780 ° C. or higher. At this time, strain is accumulated in the austenite crystal grains.

  In addition, as a result of investigating the influence of the structure on the shape of the appearance of the bent portion and the crack generated in the bending ridge line at the limit processing, when the hot-rolled steel sheet according to the present invention is used, the average plastic tangent gradient H ′ By controlling H '/ TS related to the tensile strength TS, it is possible to reduce the deflection generated around the bent portion, and by reducing the grain size of the surface layer structure, it is near the surface of the local bent portion As a result, the local deformability was improved, and it was found that the occurrence of cracks can be remarkably suppressed.

  Furthermore, it was found that the final rolling ratio (rolling ratio) in the finish rolling during production greatly affects the grain size in the vicinity of the surface layer, and the rolling ratio of the final finishing stand in the final rolling pass is 10 to 50%. It was found that it is preferable. More preferably, it is 15 to 40%.

  This is because if the rolling rate at the final finishing stand is less than 10%, the accumulation of strain in the austenite is not sufficient, and subsequent precipitation makes it difficult to precipitate and refine the ferrite. When this rolling rate is 15% or more, ferrite transformation can be further promoted.

  Conversely, if rolling is performed such that the rolling rate at the final finishing stand exceeds 50%, the durability of the rolling roll may be impaired. To avoid this, it is necessary to increase the size of the rolling equipment. It is. Moreover, it is because it will be difficult to control the shape of the steel sheet. In addition, when exact | strict steel plate shape is requested | required, it is preferable to make it 40% or less.

  And cooling to the temperature of 720 degrees C or less is completed within 0.4 second immediately after completion | finish of hot rolling. At this time, since the release of this strain is suppressed during cooling, the strain is accumulated in the austenite grains, and the transformation from austenite to ferrite is activated only when the temperature reaches 720 ° C. or less. A large number of ferrite crystal grains are generated using the accumulated strain as a nucleus to form a fine ferrite structure. In this method, it is possible to suppress the release of shear strain introduced into the steel plate during hot rolling by friction between the steel plate surface and the rolling roll surface, so that it is more in the portion closer to the surface than the center of the plate thickness. Ferrite nuclei are generated.

  Furthermore, it hold | maintains for 2 second or more in the temperature range of 600-720 degreeC after that. As a result, a desired ferrite structure that is fine and distributed in a narrow range of the crystal grain size can be obtained, and strain can be prevented from remaining in the fine ferrite structure after transformation. In addition, due to the change in the amount of ferrite nucleation in the plate thickness direction described above, a structure having a gentle grain size gradient from the plate thickness center to the surface is generated.

In addition, the cooling conditions immediately after completion | finish of hot rolling need to complete the cooling to the temperature of 720 degrees C or less within 0.4 second as above-mentioned. Conventionally, even the fastest one started cooling after 0.2 seconds or more immediately after the end of rolling, and the cooling rate was about 250 ° C./second at most. Taking a low carbon steel with an Ar ₃ point of 800 ° C. as an example, even if the hot rolling of the low carbon steel is terminated at the Ar ₃ point, while the cooling is performed from 800 ° C. to 720 ° C., Since 0.52 seconds or more had elapsed, it was difficult to complete the cooling to a temperature of 720 ° C. or less within 0.4 seconds.

  Furthermore, it is necessary to subject the obtained hot-rolled steel strip to temper rolling of 0.1 to 1.0%.

  Conventionally, temper rolling has been used to ensure the degree of flatness correction for hot-rolled steel sheets and the surface properties of cold-rolled base materials that are of concern for exterior applications. The effect of the rolling reduction mainly on the shape freezing properties of the steel sheet was investigated.

  As a result, it has been found that when the steel sheet obtained by the above-described method is subjected to temper rolling of 0.1 to 1.0%, the mechanical properties defined in the present invention can be stably obtained. If the temper rolling is less than 0.1%, the flatness of the steel sheet is lowered, and the accuracy of the parts after molding is deteriorated. On the other hand, if the temper rolling is performed exceeding the upper limit of 1.0%, the yield point elongation disappears, and for example, during local bending, the stress distribution region in the local bending tangential direction is expanded, and a springback or the like occurs. It becomes easy and shape freezing property is impaired. Oh, the upper limit of the temper rolling ratio is preferably 0.5%.

  Thus, yield point elongation lowers the plastic tangent gradient. Therefore, the amount of springback can be reduced by preventing the yield point elongation from disappearing or reducing.

  The present invention has been completed on the basis of such findings and examination / experimental results. The gist of the present invention is the following (1) to (5) hot rolled steel sheet with excellent local stretch performance and (6) to (8) hot rolled steel sheet with excellent local stretch performance. is there. Hereinafter, the present invention (1) to the present invention (8), respectively. The present inventions (1) to (8) may be collectively referred to as the present invention.

  (1) A steel plate made of carbon steel or low alloy steel containing one or more of Ti, Nb, Mo, and V in total of 0.05% or less and having ferrite as a main phase, The average grain size D (μm) of ferrite at the depth position of 1/4 of the plate thickness from the surface satisfies the following formulas (1) and (2), and the yield ratio is 0.8 or more, Local elongation performance characterized in that the average plastic tangent gradient H ′ in the range from the plastic strain after yielding 0.005 to the 65% strain of uniform elongation in the JIS No. 5 tensile test satisfies the following formula (3) Excellent hot-rolled steel sheet.

1.2 ≦ D ≦ 7 (1) Formula D ≦ 2.7 + 5000 / (5 + 350 · C + 40 · Mn) ² (2) Formula 0.10.1 ≦ H ′ / TS ≦ −2 × YR + 3.1 (3) Formula where D is 1 / th of the plate thickness from the steel plate surface. 4 shows the average grain size (μm) of ferrite at a depth of 4; C and Mn are the contents (% by mass) of each element in the steel; and H ′ is the plastic strain after yielding in the tensile test from 0.005. The average plastic tangent gradient in the range up to 65% strain of uniform elongation, TS is the tensile strength (MPa), and YR is the yield ratio.

(2) The average crystal grain size D _s (μm) of ferrite on the steel sheet surface layer and the average crystal grain size D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface are the following (4) The hot-rolled steel sheet excellent in local rolling performance according to the above (1), characterized by satisfying the formula:

D _s /D≦0.8 (4) where D _s is the average crystal grain size (μm) of ferrite on the steel sheet surface layer, and D represents the average crystal grain size (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel plate surface.

  (3) The area ratio of ferrite crystal grains satisfying the following formula (5) in the ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface is 80% or more. A hot-rolled steel sheet having excellent local rolling performance as described in (1) or (2) above.

D / 3 ≦ d ≦ 3D (5) where d is the ferrite crystal grain size (μm) and D is the surface of the steel plate. The average crystal grain size (μm) of ferrite at a depth position of ¼ of the thickness is shown.

  (4) An increase rate X (μm / min) at 700 ° C. of the average crystal grain size D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface and the average crystal grain size D (μm) A hot-rolled steel sheet that satisfies the following formula (6) and is excellent in local rolling performance of any one of the above (1) to (3).

Here D · X ≦ 0.1 ················ (6) formula, D is the average from the steel sheet surface of the ferrite in the 1/4 depth position of the sheet thickness crystal The particle size (μm) and X represents the rate of increase (μm / min) at 700 ° C. of the average crystal particle size D (μm) of the ferrite.

  (5) The surface of the hot-rolled steel sheet excellent in local rolling performance of any one of the above (1) to (4) is provided with a coating layer of Zn, Al, Zn-Al alloy or Fe-Zn alloy. Hot-rolled hot-rolled steel sheet with excellent local rolling performance.

(6) A method of producing a hot-rolled steel sheet excellent in local rolling performance by multi-pass hot rolling of a slab made of carbon steel or low alloy steel, wherein the final rolling pass is Ar ₃ points or higher and 780 ° C. or higher And then cooled to 720 ° C. or less within 0.4 seconds at a cooling rate of 400 ° C./second or more, then held at a temperature range of 600 to 720 ° C. for 2 seconds or more, and then 0.1 to 1 A method for producing a hot-rolled steel sheet excellent in local rolling performance according to any one of the above (1) to (4), characterized by performing 0.0% temper rolling.

(7) A method of producing a hot-rolled steel sheet having excellent local rolling performance by multi-pass hot rolling a slab made of carbon steel or low-alloy steel, the final rolling pass being finished and the final stand rolling rate of 10-50 And at a temperature not lower than ₃ points and not lower than 780 ° C., and then cooled to not higher than 720 ° C. within 0.4 seconds at a cooling rate of not lower than 400 ° C./second, and then in a temperature range of 600 to 720 ° C. Production of hot-rolled steel sheet excellent in local elongation performance of any one of (1) to (4) above, characterized by subjecting to temper rolling of 0.1 to 1.0% after holding for 2 seconds or more Method.

  (8) The local elongation performance, characterized by pickling hot-rolled steel sheet excellent in local elongation performance obtained by the method of (6) or (7) above and then performing hot dipping in a continuous hot dipping line. A method for producing hot-rolled hot-rolled steel sheets with excellent resistance.

  According to the present invention, it has ultrafine crystal grains, has a high yield strength with a yield strength to yield strength ratio (yield ratio) of 0.8 or more, has excellent impact absorption characteristics and shape freezing properties, and is locally It is possible to provide a hot-rolled steel sheet having excellent ductility and a method for producing the hot-rolled steel sheet.

  Furthermore, according to the present invention, it has ultrafine crystal grains, has a high yield strength with a yield strength ratio (yield ratio) of 0.8 or more, and has excellent shock absorption characteristics and shape freezing properties. In addition, it is possible to provide a hot-rolled steel sheet having a thermal stability that can withstand the heat of the welding process and the hot dipping process and having excellent local rolling performance, and a method for manufacturing the hot-rolled steel sheet.

  Below, the hot-rolled steel plate excellent in local rolling performance according to the present invention will be described. Hereinafter, “%” display of the content of each chemical component means “mass%”.

(A) About chemical composition C:
C is an element useful for promoting the refinement of ferrite crystal grains because it can lower the transformation temperature from austenite to ferrite and lower the finishing temperature of hot rolling. Moreover, it is an element for ensuring strength. For this reason, it is preferable to make it contain 0.01% or more. Moreover, in order to further promote the refinement of ferrite crystal grains, the content is preferably 0.03% or more. However, if it is contained excessively, ferrite transformation after hot rolling is delayed, the volume fraction of ferrite is lowered, and weldability is deteriorated, so it is preferably made 0.25% or less. In order to improve the workability of the weld zone, the C content is preferably 0.17% or less, and more preferably 0.15% or less.

Si:
Si is preferably contained for the purpose of improving the strength. However, if it is contained excessively, the ductility deteriorates remarkably and the problem of surface oxidation during hot rolling occurs, so the content is preferably made 3% or less. Preferably it is 2% or less, More preferably, it is 1.8% or less. The lower limit may be an impurity level. Usually, about 0.01% is mixed in the steelmaking stage.

Mn:
Mn is preferably contained to ensure strength. Moreover, since the transformation temperature from austenite to ferrite can be lowered and the finishing temperature in hot rolling can be lowered, it is preferably contained in order to promote refinement of ferrite crystal grains. However, if it is contained excessively, ferrite transformation after hot rolling is delayed and the volume fraction of ferrite is lowered, so the content is preferably made 3% or less. More preferably, it is 2.7% or less. The lower limit may be an impurity level, but when it is contained for the purpose of improving the strength, it is preferably contained at 0.5% or more.

Al:
Al may be included to improve ductility. However, if excessively contained, the austenite at high temperature becomes unstable, and it is necessary to excessively increase the finishing temperature in hot rolling, and it becomes difficult to achieve stable continuous casting. The following is preferable. The lower limit may be an impurity level. Usually about 0.01% is mixed by deoxidation process.

P:
P may be contained in order to increase the strength. However, if it is excessively contained, embrittlement due to grain boundary segregation occurs, so when it is included, the content is preferably 0.5% or less. More preferably, it is 0.2% or less, More preferably, it is 0.1% or less. The lower limit may be an impurity level. Usually, about 0.01% is mixed in the steelmaking stage.

Ti:
Ti precipitates as carbide or nitride to increase the strength, and this precipitate suppresses the coarsening of austenite and ferrite to promote the refinement of crystal grains during hot rolling, and during the heat treatment In order to suppress grain growth, it may be contained. However, if excessively contained, Ti-based carbonitrides are formed and the formability or shape freezing property tends to be impaired. Therefore, the total amount of Ti + Nb + Mo + V needs to be 0.05% or less. Preferably it is 0.03% or less, More preferably, it is 0.01% or less. The lower limit may be an impurity level. Generally about 0.001% is mixed on steelmaking.

Nb:
Nb precipitates as carbide or nitride to increase the strength, and this precipitate suppresses the coarsening of austenite and ferrite to promote the refinement of crystal grains during hot rolling, and during the heat treatment In order to suppress grain growth, it may be contained. However, if excessively contained, Nb-based carbonitrides are formed and the formability or shape freezing property tends to be impaired. Therefore, the total amount of Ti + Nb + Mo + V needs to be 0.05% or less. Preferably it is 0.03% or less, More preferably, it is 0.01% or less. The lower limit may be an impurity level. Generally about 0.001% is mixed on steelmaking.

V:
V is precipitated as a carbide to increase the strength, and since this precipitate suppresses the coarsening of ferrite and promotes the refinement of crystal grains, it may be contained. However, if excessively contained, the ductility and workability are hindered for the same reason as Ti and Nb, so the total amount of Ti + Nb + Mo + V needs to be 0.05% or less. Preferably it is 0.03% or less, More preferably, it is 0.01% or less. The lower limit may be an impurity level. Generally about 0.001% is mixed on steelmaking.

Mo:
Mo may be contained in order to precipitate MoC and increase the strength, and since this precipitate suppresses the coarsening of ferrite and promotes the refinement of crystal grains. Further, Mo may be contained because it has the effect of suppressing the coarsening of carbonitride by being combined with Ti and Nb, and has the effect of improving the production stability of the formability. However, if excessively contained, the ductility and workability are hindered for the same reason as Ti, Nb, and V, so the total amount of Ti + Nb + Mo + V needs to be 0.05% or less. Preferably it is 0.03% or less, More preferably, it is 0.01% or less. The lower limit may be an impurity level. Generally about 0.001% is mixed on steelmaking.

Cr:
Since Cr has the effect of increasing hardenability and generating martensite and bainite in the ferrite structure, it may be included for the purpose of these functions. However, since the production | generation of a ferrite will be suppressed when it contains abundantly, it is preferable to make content 1% or less. The lower limit may be an impurity level. Generally about 0.02% is mixed in steelmaking.

Cu:
Since Cu has an action of precipitating at a low temperature to increase the strength, Cu may be contained for the purpose of these actions. However, since there is a risk of causing grain boundary cracking of the slab, the content is preferably 3% or less. More preferably, it is 2% or less. In addition, when making it contain, it is preferable to make it content 0.1% or more. The lower limit may be an impurity level. Generally about 0.02% is mixed in steelmaking.

Ni:
Ni may be included for the purpose of increasing the stability of austenite at high temperatures. Moreover, when Cu is contained, it may be contained in order to prevent grain boundary embrittlement of the slab. However, since the production | generation of a ferrite will be suppressed when it contains excessively, it is preferable to make content 1% or less. The lower limit may be an impurity level. Generally about 0.02% is mixed in steelmaking.

Ca, REM, B:
Ca, rare earth elements (REM), and B may be contained in one or more kinds in order to refine oxides and nitrides precipitated during solidification and maintain the soundness of the slab. However, since it is expensive, the total content is preferably 0.005% or less. The lower limit may be an impurity level. Here, the rare earth element (REM) means 17 elements including 15 elements of lanthanide and Y and Sc.

  Other examples of “impurities” mixed in the steel include S, N, and Sn. About S and N, if possible, it is desirable to regulate the content thereof as follows.

S:
Since S is an impurity element that forms sulfide inclusions and degrades workability, the content is preferably suppressed to 0.05% or less. And when securing the further outstanding workability, it is preferable to set it as 0.008% or less. More preferably, it is 0.003% or less.

N:
N is an impurity element that lowers workability, and its content is preferably suppressed to 0.01% or less. More preferably, it is 0.006% or less.

(B) About the structure of the hot-rolled steel sheet excellent in local ductility according to the present invention The hot-rolled steel sheet excellent in local ductility according to the present invention has ferrite as the main phase, the main phase and the second phase other than ferrite. It is a steel plate which has the structure which consists of. Here, the “main phase” means that the phase occupying the maximum proportion of the phase constituting the organization is the phase. The main phase ferrite is preferably at least 50% or more by volume, more preferably 60% or more. If the ferrite volume fraction is less than 50%, the ductility and workability of the steel sheet may be impaired.

  The crystal grain size (diameter) of the ferrite greatly affects the mechanical properties and thermal stability of the hot-rolled steel sheet, and further the workability. Therefore, in order to ensure sufficient strength, ductility, thermal stability, and bending workability in the hot-rolled steel sheet according to the present invention, the average crystal grains of ferrite at a depth of ¼ of the sheet thickness from the steel sheet surface It is necessary to keep the diameter D (μm) within a certain range that satisfies the following expressions (1) and (2).

1.2 ≦ D ≦ 7 (1) Formula D ≦ 2.7 + 5000 / (5 + 350 · C + 40 · Mn) ² Equation (2) where D is the average crystal grain size (μm) of ferrite at a depth of 1/4 of the plate thickness from the steel sheet surface, and C and Mn are the contents (mass of each element in the steel) %).

That is, the certain range is a range in which 1.2 μm is the lower limit and 2.7 + 5000 / (5 + 350 · C + 40 · Mn) ² μm and 7 μm is the upper limit. In the formula (2), C and Mn each represent the content (mass%) of each element in the steel.

Here, the lower limit of the average grain size D of the ferrite is 1.2 μm. If the average grain size D is less than 1.2 μm, not only the work hardening coefficient is extremely reduced and the ductility and workability deteriorate, but also the fine ferrite structure This is because the thermal stability of the material deteriorates and the grains grow easily at a high temperature. In order to obtain more excellent ductility, workability and thermal stability, the lower limit of the average crystal grain size D of ferrite is preferably 1.5 μm. On the other hand, the upper limit of the average grain size D of ferrite is set to the smaller value of 2.7 + 5000 / (5 + 350 · C + 40 · Mn) ² μm and 7 μm. This is because a sufficient strength cannot be obtained. In order to obtain better strength, the upper limit of the average crystal grain size D of ferrite should be the upper value of the smaller one of 2.4 + 5000 / (5 + 350 · C + 40 · Mn) ² μm and 5.5 μm. Is preferred. Here, a region surrounded by a large-angle grain boundary having a crystal orientation difference of 15 ° or more is defined as one crystal grain, and a small-angle grain boundary less than 15 ° is ignored.

  In addition to the component structure (shape), the impact absorption performance has a strong correlation with the amount of plastic work during material deformation as the mechanical property value of the material. The high impact absorbing material has a high YR value when compared with the same tensile strength TS, and the mechanical properties thereof have a high yield strength YS. Therefore, the plastic work increases due to deformation during impact absorption. Therefore, in order to obtain sufficient collision absorption performance, the yield ratio YR needs to be 0.8 or more. The yield ratio YR is preferably 0.85 or more.

  During the bending process, a compressive stress is generated inside the material in the thickness direction of the material, and a tensile stress is generated outside the material. When the material is taken out of the mold, the stress distributed in the plate thickness direction is released, and a springback occurs as an elastic recovery phenomenon.

  For determining the magnitude relationship of the springback, the above-described difference in stress between the inside and outside of the material in the thickness direction of the material and the range in which the stress is generated have an effect.

  If the difference in bending internal / external stress generated during bending is large, the amount of spring back is also large. Further, it is known that this stress difference has a correlation with the ultimate stress due to bending. That is, under the same forming conditions, the higher the strength of the steel plate, the higher the ultimate stress due to processing, and the larger the spring back.

  Next, the range in which the bending stress is generated is, for example, a larger range in which the bending R is processed than when the bending R is large compared to a small one. That is, the range in which stress is generated is wide. Therefore, the amount of spring back is large. Further, it has been known that Rp / t has a strong correlation with springback as a relation of test conditions on springback. Here, Rp is the radius (mm) of the shoulder of the punch of the mold, and t is the thickness (mm) of the material. In the present specification, the bending radius R means R = Rp + t / 2.

  Therefore, at the same Rp / t, the material having the higher tensile strength TS has a larger springback amount, and for the material having the same tensile strength TS, the larger the Rp / t, the larger the springback amount.

  Here, a material having a low plastic tangential gradient characteristic will be described. A plastic tangential gradient is a tangential gradient of a stress-plastic strain curve in a tensile test of a material, and is one of the strain propagation characteristics during processing of a material. Value.

  The present invention focuses on localizing a stress generation region in bending. The present invention has found that when a bending test is carried out under the same molding conditions, a material having a low plastic tangential gradient characteristic localizes strain and narrows the range in which bending stress is generated, so that the springback is reduced. Is based on that. That is, according to the conventional knowledge, if Rp / t and tensile strength TS are the same, the same springback amount is shown. However, according to the present invention, even if these values are the same, the plastic tangent The lower the slope, the smaller the springback. Simulation analysis has revealed that the average plastic tangent gradient H ′ / tensile strength TS needs to be [−2 × YR + 3.1] or less in order to achieve both shock absorption characteristics and shape freezing properties. .

  However, when the yield strength YS and the yield ratio YR are extremely low, the difference between the internal and external stresses in the thickness direction is small, and the springback may be small regardless of the magnitude of H ′. However, in this case, since the shock absorbing performance is inferior, the steel sheet that achieves both the impact absorbing performance and the shape freezing property of the present invention is not achieved, so in the present invention, the yield strength YS and the yield ratio YR are extremely low. There is no need to assume a case.

  FIG. 10 is a simulation of the magnitude of the stress generated in the right-angle bending process for each bending position. (a) is a material having a plastic tangential gradient H ′ / tensile strength TS = 0.98 (material of the present invention), and (b) is a material having a plastic tangential gradient H ′ / tensile strength TS = 1.78 (SAPH440: JIS). G 31133). Both are hot-rolled steel sheets having a tensile strength TS of about 440 MPa. The simulation was based on a simulation analysis using a dynamic explicit general-purpose FEM code LS-DYNA ver.970.

  As can be seen from FIG. 10, in the material (a) according to the present invention, the region where the stress is generated is narrow, whereas in the comparative material (b), the region where the stress is generated is wide. Therefore, the material (a) according to the present invention has a small spring back, while the comparative material (b) has a large spring back.

  In addition, it is known that a buckling wrinkle generation behavior at the time of deformation of a part affects an efficient shock absorbing structure. As a material condition for generating an ideal buckling wrinkle, a work-hardening characteristic to some extent is required for the material. Therefore, the average plastic tangential gradient H ′ / tensile strength TS needs to be 0.1 or more. Preferably it is 0.13 or more.

  Therefore, the average plastic tangential gradient H ′ in the range from the plastic strain after yielding 0.005 to the 65% strain of uniform elongation in the JIS No. 5 tensile test needs to satisfy the following formula (3).

0.1 ≦ H ′ / TS ≦ −2 × YR + 3.1 (3) where H ′ is one from the plastic strain after yielding 0.005 in the tensile test. The mean plastic tangent gradient in the range up to 65% strain of uniform elongation, TS is the tensile strength (MPa), and YR is the yield ratio.

  Next, the local bending process such as the contact bending process will be described. In the local bending process, as in the case of the right-angle bending process, during the local bending process, a compressive stress is generated inside the local bend in the plate thickness direction of the material, and a tensile stress is generated outside the local bend. When the material is taken out of the mold, the stress distributed in the plate thickness direction is released, and a springback occurs as an elastic recovery phenomenon.

  For determining the magnitude relationship of the springback, the above-described difference in local bending internal / external stress in the thickness direction of the material and the range in which the stress is generated have an effect.

  If the local bending internal / external stress difference generated during local bending is large, the amount of spring back is also large. Further, it is known that this stress difference has a correlation with the ultimate stress due to local bending. That is, under the same forming conditions, the higher the strength of the steel plate, the higher the ultimate stress due to processing, and the larger the spring back.

  Next, the range in which the local bending stress is generated is, for example, a larger range in which the local bending direction is processed than when the local bending R is large, compared to a small range. That is, the range in which stress is generated is wide. Therefore, the amount of spring back is large. Therefore, as for the relationship of the local bending test conditions on the springback, it has been found that Rp / t has a strong correlation with the springback as in the case of the right-angle bending process. Here, Rp means the radius (mm) of the shoulder of the punch of the mold, t means the plate thickness (mm) of the material, and the local bending radius R means R = Rp + t / 2 This is the same as in the right angle bending process.

  Even in the close contact bending process, the size of the spring back is determined by the distribution of (i) the difference in the thickness direction of the residual stress in the local bending direction (the difference between the residual stress inside the local bend and the residual stress outside the local bend), and (ii It is determined by the distribution in the local bending direction of the region where the difference in residual stress between the inside and outside of the local bending occurs.

  Therefore, if the residual stress and the local bending direction in the tight bending process can be controlled, the springback can be reduced as in the case of the right angle bending.

  Residual stress varies depending on the behavior of local bending deformation during close contact bending, but as with right angle bending, the difference in residual stress inside and outside the local bending in (i) is the same as when the material is subjected to local bending. It is known that there is a correlation with the local bending part ultimate stress. In addition, since the material with low work hardening characteristics has a narrow deformation region, the strain is likely to be localized, and the region where the local bending internal / external residual stress difference (ii) occurs can be localized. The amount can be reduced.

  Excellent local extension performance means that in such close contact bending, cracking is suppressed on the outer side of the bend and the bent part becomes sharper, and the springback amount is low, so the sharper shape is It also means that it has a shape freezing property of being maintained.

  Since the local elongation performance is considered to be the elongation performance in a minute region near the fracture portion, the local elongation performance can also be evaluated by performing the following test.

  FIG. 11 shows the situation before and after the tension of a JIS No. 5 tensile test piece for evaluating the local elongation performance. (a) is in a state before tensioning, and (b) is in a state in which it is pulled until just before breaking.

  A dot-like marking is given to the JIS No. 5 tensile test piece before the tensile test at intervals of 1 to 2 mm, and the tensile test is carried out until just before the test piece breaks, and then the marking interval after the test is measured. By comparing the marking intervals on the strain measurement line before and after the test, it is possible to obtain the strain distribution of the minute region of the test piece.

  FIG. 12 shows a strain (deformation) distribution of a minute region at the center in the width direction of the test piece. The material of the present invention is a material having a plastic tangential gradient H ′ / tensile strength TS = 0.98, and the comparative material is usually a material having a plastic tangential gradient H ′ / tensile strength TS = 1.78 (SAPH440: JIS G 31133). . The material of the present invention can recognize a concentration of strain as compared with the normal comparative material. Furthermore, the material of the present invention has a larger absolute value of strain near the fractured portion (center O) than that of the normal comparative material.

  From this, it can be seen that the material of the present invention has a small amount of springback and suppresses the occurrence of cracks in the local bent portion. In addition, since the occurrence of cracks in the local bends is the starting point of fracture at the interface between the soft part and the hard part in the crystal structure, the suppression of the occurrence of cracks in the local bends is very It means that it has a uniform structure.

  The present inventors have conducted various studies and experiments in order to obtain excellent local elongation performance, and as a result, the average plastic tangential gradient H ′ and the crystal grain size of the steel sheet have a correlation with this local elongation performance. It has been found that That is, in the case of the low H ′ material, when the steel plate is bent, the strain concentrates in a narrow range of the local bending portion, thereby reducing the amount of springback and the fine grain size of the steel plate. Since the absolute value of the strain in the tensile direction becomes large because it is uniform, the occurrence of cracks in the local bending portion is suppressed and the local bending portion is considered to have a sharp shape.

Furthermore, in order to make the local ductility more excellent, the average crystal grain diameter D _s (μm) of the ferrite on the steel sheet surface layer is set to the average crystal grain of the ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface. It is preferable to stay within a certain range with respect to the diameter D (μm). In order to further suppress the occurrence of cracks in the local bending portion, it can be achieved by making the average crystal grain size of ferrite on the surface of the steel sheet finer than the average crystal grain size of ferrite inside the steel sheet.

That is, the average crystal grain diameter D _s (μm) of ferrite on the steel sheet surface layer and the average crystal grain diameter D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface are expressed by the following formula (4): Is preferably satisfied.

D _s /D≦0.8 (4) where D _s is the average crystal grain size (μm) of ferrite on the steel sheet surface layer, and D represents the average crystal grain size (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel plate surface.

In order to further improve the thermal stability of the steel sheet, it is preferable to keep the distribution of the crystal grain size of ferrite within a certain range. One factor that causes grain growth at high temperatures is the driving force based on the energy of the grain boundaries.If relatively large ferrite crystal grains are mixed in a fine ferrite structure, the large ferrite crystal grains As a driving force, it easily integrates with the surrounding fine ferrite crystal grains, and the grain growth proceeds rapidly. Therefore, to suppress the growth rate of ferrite crystal grains at high temperature, the ferrite crystal grains are refined and the average crystal grain size D (μm) satisfies the above formulas (1) and (2). In addition to staying within a certain range, the crystal grain size d (μm) of the ferrite at the depth position of ¼ of the plate thickness from the steel plate surface is occupied by crystal grains satisfying the following formula (5) The area ratio is preferably 80% or more.
D / 3 ≦ d ≦ 3D (5) where d is the ferrite crystal grain size (μm) and D is the surface of the steel plate. The average crystal grain size (μm) of ferrite at a depth position of ¼ of the thickness is shown.

  That is, it is preferable that the grain size distribution is such that 80% or more of the ferrite crystal grains fall within the range of 1/3 to 3 times the average crystal grain size D (μm) in terms of area ratio. Preferably, the grain size distribution is such that 85% or more of the ferrite crystal grains fall within a range of 1/3 to 3 times the average crystal grain diameter D (μm), more preferably 90% or more of the ferrite crystal grains. Is a particle size distribution that falls within a range of 1/3 to 3 times the average crystal grain size D (μm).

  The reason for defining the ferrite crystal grain size and its distribution as a depth of 1/4 of the plate thickness from the surface is that the ferrite crystal grain size of the hot-rolled steel sheet generally changes in the plate thickness direction. The steel sheet according to the present invention can ensure desired mechanical properties and thermal stability by setting the ferrite crystal grain structure of this depth in the above range. In particular, the thermal stability of the particle size is not determined by the particle size distribution when taking statistics over a wide range from the surface of the plate to the inside, but by the particle size distribution when taking statistics at a specific depth. Determined. Therefore, if the structure is observed in a cross section parallel to the surface at a depth of 1/4 of the plate thickness, or if it is observed in a cross section perpendicular to the surface, it is within 100 μm from the depth of 1/4 of the plate thickness. Make observations and take statistics.

  The gradual change in crystal grain size in the thickness direction contributes to the improvement of the mechanical properties of the steel plate. For example, since it is finer on the plate surface side, local bendability in which the vicinity of the steel plate surface is greatly deformed is improved. In addition, the propagation of cracks generated from the vicinity of the surface can be effectively suppressed by the finer surface structure, so that fatigue characteristics are also improved.

Therefore, the crystal grain size d _s (μm) at a depth position of 100 μm from the steel plate surface, the crystal grain size d (μm) at a depth position of ¼ of the plate thickness from the steel plate surface, and the crystal grains at the center portion of the plate thickness The diameter d _c (μm) preferably satisfies the following expressions (7) and (8).

_{d s ≦ 0.7d c ················ (7} ) formula d ≦ 0.9d _c ················ ( 8) where d _s is the crystal grain size (μm) at a depth of 100 μm from the steel sheet surface, d is the crystal grain size (μm) at a depth position of ¼ of the plate thickness from the steel sheet surface, Then, d _c denotes the crystal grain size in the central portion of the thickness ([mu] m).

Incidentally, the causes have grain diameter change of the thickness of the plate that satisfies _{d s} ≦ 0.6d _c and d ≦ 0.85d _c, more preferably.

  The second phase other than ferrite may be a phase generally known to be produced in a low-carbon steel material, such as pearlite, cementite, bainite, martensite, retained austenite, or carbonitride of an element other than Fe.

  In order to efficiently produce a steel sheet having a yield ratio of 0.8 or more and excellent mechanical properties and thermal stability and excellent shape freezing property, the amount of the second phase is preferably less than 20%. This is because when the amount of the hard second phase is large during temper rolling applied during production, the shape freezing property becomes sensitive to rolling conditions such as the temper rolling ratio, and the production load increases. Since this becomes more conspicuous as the second phase hardness increases, for example, the second phase is preferably bainite rather than martensite.

As the second phase other than ferrite, a trace amount of carbide, nitride, or oxide having a volume ratio of 1% or less can be contained in addition to the above-described one. These include Ti, Nb, V, Mo carbonitrides and the like.
(C) Grain growth rate at high temperature The temperature characteristics of the grain growth rate of a steel sheet in which the average crystal grain size of ferrite is within a certain range satisfying the above equations (1) and (2) is around 700 ° C. It is determined by the grain growth rate of ferrite at the following temperature.

  Therefore, when heated to a higher temperature in the welding process or the hot dipping process, the rate of increase in the average crystal grain diameter D (μm) of ferrite at 700 ° C. at a depth position of ¼ of the sheet thickness from the steel sheet surface. It is preferable that X (μm / min) and the average crystal grain size D (μm) satisfy the following formula (6).

Here D · X ≦ 0.1 ················ (6) formula, D is the average from the steel sheet surface of the ferrite in the 1/4 depth position of the sheet thickness crystal The particle size (μm) and X represents the rate of increase (μm / min) at 700 ° C. of the average crystal particle size D (μm) of the ferrite.

That is, by maintaining the product D · X (μm ² / min) of the increase rate X (μm / min) of the average crystal grain size of ferrite and the average crystal grain size D (μm) at 0.1 μm ² / min or less. , It becomes stable against the main thermal history in the welding and hot dipping process, and good thermal stability is obtained. In order to obtain better thermal stability, the product D · X is preferably 0.07 μm ² / min or less, and more preferably 0.05 μm ² / min or less.

In addition, as shown in Examples 2 and 3 to be described later, the product D · X (μm ² / min) of the increase rate X (μm / min) of the average crystal grain size of ferrite and the average crystal grain size D (μm) However, the ferrite crystal grain structure of the steel sheet of 0.1 μm ² / min or less shows almost no change in grain size even when heat-treated at 850 ° C. for several tens of seconds. Unlike normal grain growth, which is proportional to the square root of time, the crystal grain size (diameter) of ferrite in the steel sheet according to the present invention increases at approximately 700 ° C. in proportion to time. Therefore, the increase rate X (μm / min) of the average crystal grain size of ferrite is obtained by measuring the grain size change at about 700 ° C. for about 1 hour and averaging the rate of change.

In order to further reduce the grain growth rate, the dislocation density in the ferrite crystal grains is preferably 10 ⁹ / cm ² or less, more preferably 10 ⁸ / cm ² or less.

(D) About rolling Rolling is performed in the austenite temperature range using a lever mill or a tandem mill from a temperature exceeding 1000 ° C. From the viewpoint of industrial productivity, it is preferable to use a tandem mill for at least the last several stages.

Use slabs obtained by continuous casting or casting / bundling, steel plates obtained by strip casting, etc., and if necessary, those once hot or cold worked, and if they are cold pieces, 1000 ° C Reheated to a temperature exceeding 30 ° C and rolled. When the rolling start temperature is 1000 ° C. or less, the rolling load becomes excessive and it becomes difficult to obtain a sufficient rolling rate, and rolling at a sufficient rolling rate may be terminated at a temperature of ₃ or more points at Ar. This makes it difficult to obtain desired mechanical properties and thermal stability. Rolling is preferably started at a temperature of 1025 ° C. or higher, more preferably 1050 ° C. or higher. The upper limit is set to 1350 ° C. or lower, preferably 1250 ° C. or lower in order to suppress coarsening of austenite grains and to suppress equipment costs and heating fuel costs. In the case of a steel type in which it is not necessary to sufficiently dissolve precipitates such as TiC and NbC in austenite, it is preferable to reheat to a relatively low temperature (1050 to 1150 ° C.) within this range. This is because the initial austenite crystal grains are refined and the final ferrite crystal grains are easily refined.

The rolling finishing temperature is set to a temperature range of Ar ₃ points or more and 780 ° C. or more in order to transform from austenite to ferrite after rolling. When the finishing temperature is lower than Ar ₃ point, ferrite is generated during rolling. If the temperature is lower than 780 ° C., the rolling load increases and it becomes difficult to apply sufficient reduction, and ferrite transformation may occur in the surface layer portion during rolling. Preferably, the rolling is finished at a temperature of Ar ₃ points or higher and 800 ° C. or higher.

The temperature to terminate the rolling, the better low if the temperature range of more than Ar ₃ point and 780 ° C.. This is because the effect of accumulating processing strain introduced into austenite by rolling increases, and the refinement of crystal grains is promoted. The Ar ₃ point of the steel type used in the present invention is approximately 780 to 900 ° C.

  The total reduction amount is 90% or more, preferably 92%, more preferably 94% or more in terms of sheet thickness reduction rate in order to promote the refinement of ferrite. The sheet thickness reduction rate in the temperature range from the rolling end temperature to “rolling end temperature + 100 ° C.” is preferably 40% or more. More preferably, the sheet thickness reduction rate in the temperature range from the rolling end temperature to “rolling end temperature + 80 ° C.” is 60% or more. The rolling is continuous multi-pass rolling. The amount of reduction per pass is preferably 15 to 60%. A larger rolling reduction per pass is preferable from the viewpoint of accumulating strain into austenite and refining the crystal grain size of ferrite produced by transformation. Not only increases in size, but also makes it difficult to control the shape of the plate.

  In addition, it is preferable that the rolling rate of the finishing final stand is 10 to 50% in the final rolling pass. More preferably, it is 15 to 40%. This is based on the knowledge that the occurrence of cracks in the locally bent portion can be remarkably suppressed because the local deformability in the vicinity of the surface of the locally bent portion is improved by refining the particle size of the surface layer structure.

  However, if the rolling rate at the final finishing stand is less than 10%, the accumulation of strain in the austenite is not sufficient, so that subsequent precipitation makes it difficult to precipitate and refine the ferrite. If the rolling rate is 15% or more, ferrite transformation can be further promoted.

  On the contrary, if rolling is performed such that the rolling rate at the finishing final stand exceeds 50%, the durability of the rolling roll may be impaired, and in order to avoid this, it is necessary to enlarge the rolling equipment. Moreover, it is expected that control of the steel plate shape will be difficult.

  In the method of the present invention, fine ferrite crystal grains can be obtained even by rolling in a plurality of passes with a reduction amount per pass of 40% or less. Therefore, in particular, when it is desired to easily control the plate shape, it is preferable to set the rolling reduction rate of the final two passes to 40% / pass or less.

(E) Cooling after rolling In order to generate a fine ferrite grain structure by transforming from austenite to ferrite as a driving force without releasing the processing strain introduced into austenite after rolling is completed. Then, it is cooled to a temperature of 720 ° C. or less within 0.4 seconds from the end of rolling. Preferably, it is cooled to a temperature of 720 ° C. or less within 0.2 seconds from the end of rolling. It is desirable to use water cooling for cooling, and the cooling rate is preferably 400 ° C./second or more as an average cooling rate during the period of forced cooling excluding the air cooling period.

  Here, the reason for prescribing the time until cooling to a temperature of 720 ° C. or lower was introduced by processing before fine ferrite was formed when cooling was stopped or slowed at a temperature exceeding 720 ° C. This is because the strain is released or the existence form of the strain is changed, so that it becomes ineffective for nucleation of ferrite and the ferrite crystal grains are remarkably coarsened.

  When the temperature reaches 720 ° C. or lower, it enters a transformation temperature range in which ferrite transformation is activated. The ferrite transformation temperature range where the above ferrite structure is obtained is a temperature range between this temperature and 600 ° C. Therefore, after reaching 720 ° C. or lower, the cooling is temporarily stopped, or the speed thereof is slowed down and held at this temperature range for 2 seconds or more, so that the formation of the above thermally stable ferrite crystal grain structure is ensured. Can be. If the holding time in this temperature range is short, the formation of the thermally stable ferrite crystal grain structure may be hindered. More preferably, it is good to make it stay for 3 seconds or more in the temperature range of 620-700 degreeC.

(F) About cooling equipment In this invention, the equipment which performs said cooling is not limited. Industrially, it is preferable to use a water spray device having a high water density. For example, it is possible to cool by arranging a water spray header between the rolled plate conveying rollers and injecting high-pressure water having a sufficient water density from above and below the plate.

(G) Regarding temper rolling By subjecting the obtained hot-rolled steel strip to temper rolling, the present invention can be effectively expressed.

  Conventionally, temper rolling has been used for the purpose of flattening for hot-rolled steel sheets and for improving the surface properties of cold-rolled base materials that are concerned in exterior applications. Regarding the fine-grained steel sheet, the influence of the rolling reduction on the steel sheet structure, impact absorption characteristics and shape freezing characteristics was examined in particular during the temper rolling.

  As a result, the yield strength (impact absorption characteristics) has a downward convex characteristic with the increase in steel sheet elongation (temper rolling ratio) during temper rolling, and with the increase in temper rolling ratio, The shape freezing index H ′ tended to increase (shape freezing decreased). Further, it has been found that as the amount of the second phase in the structure and its hardness increase, the increase in H ′ (decrease in shape freezeability) accompanying the increase in the temper rolling ratio becomes more significant. Therefore, in order to balance the impact absorption characteristics and the shape freezing property, it was found that the control of the temper rolling together with the steel structure is important.

  As a result of further proceeding with such examination, while maintaining the shape accuracy of the steel sheet, from the balance of yield strength (impact absorption characteristics) and H ′ shape freezing property, temper rolling is controlled to 0.1 to 1.0%, The inventors have found that the characteristics specified in the present invention can be stably obtained, and obtained the knowledge that the characteristic stability against temper rolling is further improved when the amount of the second phase is less than 20% in the steel structure. .

  That is, when the temper rolling is less than 0.1%, the flatness of the steel sheet is lowered, and the accuracy of the parts after molding is deteriorated. On the other hand, when the temper rolling is performed exceeding 1.0%, the upper limit of the formula defined in the present invention is exceeded, the stress distribution region during processing is expanded, and spring back is likely to occur and the shape freezing property is impaired. The upper limit of temper rolling is preferably 0.5%.

(H) About Zn plating The hot rolled steel sheet having the above-mentioned structure and its thermal stability and excellent in local elongation performance is obtained by using a hot dipping line, Zn, Zn-Al alloy, Al-Si alloy, Fe-Zn. It is possible to coat the steel sheet surface with an alloy or the like.

As a composition of the plating bath of the Zn—Al alloy, a Zn— (0.1-60)% Al bath, a bath in which Si and / or Mg are added in combination, and the like are used. Moreover, as a composition of the plating bath of the Al—Si alloy, an Al— (7-13)% Si bath or the like is used. There is no particular problem even if the plating bath contains 0.1% or less of Fe, V, Mn, Ti, Nb, Ca, Cr, Ni, W, Cu, Pb, Sn, Cd, and Sb. The composition of the film on the surface of the steel sheet cooled after the plating generally has a slightly higher Fe concentration than the plating bath composition, because interdiffusion of elements occurs between the steel material and the molten metal during immersion and cooling. The alloyed hot dip galvanizing positively utilizes this mutual diffusion, and the Fe concentration in the film is 7 to 15%. Although the amount of plating is not particularly limited, it is preferably 30 to 200 g / m ² per side, and in the case of alloyed hot dip galvanizing, there is a concern about powdering, so 25 to 60 g / m. ² is preferable.

  The plating method using the hot dipping line is as follows.

A hot-rolled steel sheet having a fine grain structure and excellent local rolling performance is passed through a continuous hot-dip galvanizing line after removing the surface scale through a pickling process. From the entry side, after alkali degreasing and washing with water, after preheating, it is heated to a temperature of 550 to 900 ° C. in an atmosphere containing hydrogen, and the Fe oxide on the steel sheet surface is reduced, which is suitable for the subsequent plating treatment. Forming a surface. When the temperature is lower than 550 ° C., the reduction is not sufficient, and when heated to a temperature exceeding 900 ° C., the ferrite structure becomes coarse. In order to obtain a ferrite + pearlite structure or a ferrite + cementite structure after plating, the temperature is preferably from 550 ° C. to around 730 ° C. On the other hand, bainite as a second phase, martensite, to thereby produce a residual γ, etc., who are heated from _point A to a two-phase coexisting temperature region of ferrite and austenite to 900 ° C. are preferred. The hydrogen content in the atmosphere is preferably 5 to 40%. If the hydrogen content is less than 5%, the reduction is not sufficiently performed. If it exceeds 40%, the cost of the atmospheric gas increases excessively. Components other than hydrogen may be any gas that does not inhibit reduction. Nitrogen is preferred from the viewpoint of cost. The soaking time is not particularly specified as long as the reduction is sufficiently performed, and is generally 10 seconds or longer. The upper limit is 5 minutes or less, more preferably 2 minutes or less in order not to coarsen the ferrite. After passing through heating and soaking for this reduction, the steel sheet temperature is cooled to the vicinity of the plating bath temperature, adjusted to a predetermined adhesion amount after being immersed in the plating bath, and cooled to room temperature. In the case of alloying hot dip galvanizing, after hot dip galvanizing as described above, reheating to 470 to 600 ° C. causes a reaction between the base iron and the plating film, and the Fe—Zn alloy film is formed on the steel sheet surface. Form.

  Thus, in the hot dipping method, the steel sheet is not only heated in the plating bath, but also in the process of reducing the surface oxide layer before being immersed in the plating bath, and in the alloying step after immersion in the plating bath, high-temperature heat treatment. Receive. However, since the ferrite structure of the steel sheet of the present invention is thermally stable, the fine grain structure is maintained even after these steps and exhibits excellent mechanical properties. Further, since the ferrite crystal grains on the surface are fine, the alloying reaction rate is increased, and there is an advantage that the production can be efficiently performed.

  The steel composition for plating is C: 0.001 to 0.15%, Si: 0.005 to 1.5% and / or P: 0.005 to 1.0%. Is preferred.

(I) About weldability In the steel plate which has the fine grain structure created by the conventional low temperature rolling, since it is inferior to thermal stability and a HAZ part softens, the characteristic of a welded part will fall. On the other hand, the thermal stability of the steel sheet according to the present invention is good even when the steel sheet itself or the steel sheet with the above-mentioned surface coating is joined by welding, and welding such as laser, spot, arc, etc. The formability of the welded part after welding is improved.

  Hereinafter, the present invention will be described in more detail by way of examples.

  Steels of steel types A1 to A11 having chemical compositions shown in Table 1 were melted and made 30 mm thick by hot forging. Then, after reheating to 1050 degreeC or more, it rolled by the small tandem mill for a test, and finished to 2 mm of plate | board thickness.

Table 2 shows the rolling finishing temperature and cooling conditions. In all rolling, the finishing temperature of rolling was higher than the Ar ₃ point of each steel type, and further, multi-pass rolling of 3 passes or more was performed within the temperature range of finishing temperature to [finishing temperature + 100 ° C.]. The final two-pass rolling was light rolling at 35% / pass or less except for test number 3. For test number 3, the final two passes were 50% to 60% large rolling. In test No. 18, the rolling rate of the final stand was particularly lightly reduced.

  After the rolling finish, as shown in Table 2, it was cooled to a predetermined temperature within a temperature range of 500 to 720 ° C. by water cooling. Depending on the test number, a holding time at 600 to 720 ° C. was provided by providing an air cooling time after water cooling. In Table 2, in addition to the holding time in the temperature range of 720 to 600 ° C., the holding time in the temperature range of 620 to 700 ° C. is also shown. Thereafter, water cooling to room temperature is performed at a rate of about 100 ° C./s, or by performing furnace cooling in the furnace after water cooling to a predetermined temperature within a temperature range of 400 to 600 ° C. A steel sheet having the following structure was prepared.

About the structure | tissue of the hot-rolled steel plate obtained in this way, the cross section of the steel plate thickness was observed by using a scanning electron microscope.

  The crystal grain size and the grain size distribution of ferrite were obtained by conducting crystal orientation analysis using the EBSP (Electron Back Scattering Pattern) method at a depth of ¼ of the plate thickness from the plate surface. The volume ratio of each phase was measured by observing a structure corroded with nital or picric acid at a depth of 1/4 of the plate thickness from the plate surface using a scanning electron microscope. The structure of the second phase other than the ferrite phase of the steel sheet produced in this example was pearlite, bainite, and intragranular spherical cementite or grain boundary cementite.

Further, for the steel sheet of the present invention, the average crystal grain diameter D _s (μm) of ferrite on the steel sheet surface layer, and the average crystal grain diameter D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface Was measured by the same method as described above. Then, D _s / D was calculated.

  Furthermore, regarding the steel plate of the present invention, the crystal grain size at a depth of 100 μm from the steel plate surface and the crystal grain size at the center of the plate thickness were measured by the same method as described above. As a result, for all the steel sheets of the present invention, the crystal grain size at a depth of 100 μm is 70% or less of the grain size at the thickness center, and the grain size at a depth of ¼ of the thickness is the grain size at the thickness center. It was 90% or less.

  For mechanical properties, tensile properties were measured with JIS No. 5 tensile test pieces, and tensile strength TS (MPa), yield ratio YR and total elongation El (%) were evaluated.

For thermal stability, after immersing in a salt bath at 700 ° C. for 10, 30 or 60 minutes, quench, measure the particle size by the same method as described above, and determine the pre-annealing particle size d ₀ (μm) and annealing. The increase rate X (μm / min) of the average crystal grain size of the ferrite was calculated by dividing the difference in the post grain size d ₁ (μm) by the annealing time (min).

  Table 3 shows the structure, properties, and tensile test results of the hot-rolled steel sheet thus obtained. Here, since test number 1 has a short retention time of 0.7 seconds in the temperature range of 600 to 720 ° C., the ferrite volume fraction is not only as small as 14.2%, but also the grain growth when annealed at 700 ° C. High speed and poor thermal stability. Test No. 3 employs large rolling at low temperature, so the particle size is excessively fine, 1.22 μm, and is inferior in thermal stability and strength / elongation balance. In Test No. 18, the average crystal grain size of the ferrite on the surface layer is coarse, and the local ductility is inferior.

  In contrast to these comparative examples, the inventive examples in which the cooling conditions are within the scope of the present invention are excellent in both thermal stability and mechanical properties.

  Furthermore, the test was implemented about the local elongation performance of the steel plate. The local elongation performance of the steel sheet was determined by the adhesion bending test method.

  The adhesion bending test was performed by bending the test piece at 90 degrees with a V-bending mold and then bending the specimen with the adhesion bending mold until the test piece was adhered.

  FIG. 13 shows a procedure for bending the test piece 1 to 90 degrees with a V-bending mold. (A) After placing the test piece 1 on a die 2 having a V-shaped female die, b) The test piece is bent at 90 degrees by applying a punch 3 having a V-shaped male shape to the test piece 1.

  FIG. 14 shows a procedure for closely attaching the test piece 1 bent at 90 degrees in this manner. (A) The test piece 1 bent at 90 degrees is attached to the upper mold 4 and the lower mold of the close-contact bending mold. (B) The test piece 1 is bent with the upper mold 4 and the lower mold 5 until they are in close contact with each other.

  The method for judging the result of the adhesion bending test is as follows. As a phenomenon that becomes a problem in close contact bending, there is a crack due to insufficient local ductility of a bent portion.

FIG. 15 shows an example of a problem in close contact bending. If even a slight crack occurs, the component functions (component strength, component rigidity, fatigue characteristics) as a product are significantly impaired. Therefore, the local extension performance is evaluated by the presence or absence of the occurrence of cracks as follows.
○: No crack x: Crack present Table 3 shows the results of the adhesion bending test. In addition, the plate | board thickness of the material in this test is 1.6 mm altogether. Good results were obtained for all the inventive materials.

A steel piece (size: 80 mm width × 100 mm length × 35 mm thickness) having a chemical composition shown in Table 4 is hot-rolled at the temperature of Ar ₃ or higher under the conditions shown in Table 5 (final 2 The rolling of the pass was light rolling at 35% / pass or less), followed by water cooling to obtain a hot rolled steel sheet having a sheet thickness of 1.2 mm.

The obtained hot-rolled steel sheet was measured for ferrite average crystal grain size, its grain size distribution and dislocation density at a depth of ¼ of the plate thickness from the plate surface, and thermal stability was evaluated. . The ferrite crystal grain size, the grain size distribution and the dislocation density were measured, and the thermal stability was evaluated by the same method as described above. The dislocation density ρ (cm ⁻² ) was determined by measuring the number L of intersection points between the length L (cm) of an arbitrary line segment and the dislocation line in a bright field image by observation with a transmission electron microscope, and measuring the film thickness t ( cm) was obtained according to the following equation (9).

ρ = 2N / Lt (9) where ρ is the dislocation density (cm ⁻² ), and N is the intersection N with the dislocation line. , L represents the length (cm) of an arbitrary line segment, and t represents the film thickness (cm). For the steel sheet of the present invention, the average crystal grain diameter D _s (μm) of ferrite on the surface layer of the steel sheet The average crystal grain diameter D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel plate surface was measured by the same method as described above. Then, D _s / D was calculated.

Regarding the thermal stability of the ferrite crystal grains, after immersion in a salt bath at 700 ° C. for 10, 30 or 60 minutes, the ferrite grains are rapidly cooled, the particle diameter is measured by the same method as described above, and the grain diameter before annealing d ₀ ( (μm) and the grain size d ₁ (μm) after annealing were divided by the annealing time (min) to calculate the increase rate X (μm / min) of the average crystal grain size of ferrite.

  Regarding the steel sheet of the present invention, the crystal grain size at a depth of 100 μm from the steel sheet surface and the crystal grain size at the center part of the plate thickness were measured by the same method as described above. As a result, the crystal grain size at a depth of 100 μm is 60% or less of the grain size at the center of the plate thickness, and the grain size at a depth of ¼ of the plate thickness is the grain size at the center of the plate thickness. It was 85% or less.

  In order to clarify the influence of the heat treatment on the mechanical properties of the hot-rolled steel sheet thus obtained, the reheat treatment was performed in the range of 730 to 830 ° C., and then the ferrite average crystal grain size was measured again. . Here, as for the mechanical properties, tensile properties were measured with a JIS No. 5 tensile test piece, and the tensile strength TS (MPa), the yield ratio YR, and the total elongation El (%) were evaluated.

  Table 6 shows the structure, properties and tensile test results of the hot-rolled steel sheet thus obtained, and after reheating treatment in the range of 730 to 830 ° C., the average ferrite grain size was measured again. The results are shown. Here, in test numbers C and F, the steel sheet after hot rolling is inferior in mechanical properties and thermal stability. Then, it was confirmed that the reheat treatment increased the ferrite crystal grain size to more than 8 μm and further deteriorated the mechanical properties. In contrast to these comparative examples, the steel sheet having excellent thermal stability according to the present invention exhibits excellent mechanical properties and has a particle size of almost no grain even after heat treatment at 730 ° C. to 830 ° C. for several tens of seconds. No change is shown. Therefore, it was confirmed that the steel sheet according to the present invention was strengthened with fine grains even after the heat treatment.

  Moreover, since it was confirmed that H 'was low for the test numbers I, J and K subjected to plating, it can be theoretically said that the amount of springback is reduced when subjected to the same plastic strain. I understood.

  Furthermore, the test was implemented about the local elongation performance of the steel plate. The local elongation performance of the steel sheet was based on the adhesion bending test method and the evaluation method described above. In addition, the plate | board thickness of the material in this test is 1.6 mm altogether. As shown in Table 6, all the inventive materials had good results.

A steel piece (size: 80 mm width × 100 mm length × 35 mm thickness) made of a steel type having the chemical composition shown in Table 7 is hot-rolled at a temperature of ₃ or more points of Ar under the conditions shown in Table 8, and then water-cooled to obtain a plate thickness A 2.0 mm hot-rolled steel sheet was obtained. The results are shown in Table 9.

  The crystal grain size and grain size distribution of ferrite were determined by conducting crystal orientation analysis using the EBSP (Electron Back Scattering Pattern) method at a depth of ¼ of the plate thickness from the plate surface. The volume ratio of each phase was measured by observing a structure corroded with nital or picric acid at a depth of 1/4 of the plate thickness from the plate surface using a scanning electron microscope. The structure of the second phase other than the ferrite phase of the steel sheet produced in this example was pearlite, bainite, and intragranular spherical cementite or grain boundary cementite.

  Regarding the steel plate of the present invention, the crystal grain size at a depth of 100 μm from the steel plate surface and the crystal grain size at the center of the plate thickness were measured by the same method as described above. As a result, the crystal grain size at a depth of 100 μm is 70% or less of the grain size at the center of the plate thickness for all the steel plates of the present invention, and the grain size at the depth of ¼ of the plate thickness is the grain at the center of the plate thickness. It was 90% or less of the diameter.

Further, for the steel sheet of the present invention, the average crystal grain diameter D _s (μm) of ferrite on the steel sheet surface layer, and the average crystal grain diameter D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface Was measured by the same method as described above. Then, D _s / D was calculated.

  For mechanical properties, tensile properties were measured with JIS No. 5 tensile test pieces, and tensile strength TS (MPa), yield ratio YR and total elongation El (%) were evaluated.

Regarding thermal stability, after immersing in a salt bath at 700 ° C. for 10, 30 or 60 minutes, rapidly cool, measure the particle size by the same method as described above, the particle size d ₀ (μm) before annealing and the particles after annealing By dividing the difference of the diameter d ₁ (μm) by the annealing time (min), an increase rate X (μm / min) of the average crystal grain size of the ferrite was calculated.

Moreover, the test was implemented about the local extended performance of the steel plate. The local elongation performance of the steel sheet was based on the adhesion bending test method and the evaluation method described above. In addition, the plate | board thickness of the material in this test is 1.6 mm altogether. As shown in Table 9, the inventive materials all showed good results.
Further, a test was conducted on the shape freezing property of the steel sheet. The shape freezing property was evaluated by the amount of springback in the bending test.

  The bending test method was a U bending test method. The U-bending test method is a test in which a material is bent up to a right angle, and is used as one of the most general methods for evaluating shape freezing property, particularly spring back. Here, the close contact bending described in the present invention is a process of bending a material to nearly 180 °, and the difference from the U bending test can be said to be a test in which only the bending angle is different.

  Therefore, it can be said that there is no problem even if the shape freezing property evaluation in the close contact bending of the material of the present invention is performed using the U bending test which is one of the most general evaluation test methods in the bending test. .

  A specific U-bending test method is shown in FIG. FIG. 15 shows the bottom dead center state in the U bending test. a is a punch, b is a die, c is a pad, and d is a test piece. FIGS. 15 (a) and 15 (b) both show a state during the bending test. The test piece d is pressed with a pad c and a punch a so that the test piece d is not bent at the bottom of the punch. Mold. FIG. 15 (a) shows a case of bending at a right angle, and FIG. 15 (b) shows a case of bending at 60 °.

  Next, FIG. 16 shows a method for measuring the amount of springback. FIG. 16 (a) shows a case of bending at a right angle, and FIG. 16 (b) shows a case of bending at 60 °. Both show the state after the end of the bending test, and it can be seen that springback occurs in the test piece d. The dotted line is before springback, and the solid line is after springback (the state after elastic recovery after release). Here, the angle θ after elastic recovery after releasing from the mold is assumed to be the springback amount. The test conditions were processed at a right angle and carried out in the range of Rp / t in general press molding, and the thickness of the test piece was 1.4 mm.

  The test results are shown in Table 10. θ is the amount of springback, and ◯ to x were judged according to the springback criteria set under each Rp / t condition.

The criteria for determining springback are as follows. In each Rp / t condition, when more springback occurs than this, a value that makes it difficult to reduce the springback due to the prospect of the mold or the like is regarded as a springback failure.
○: Spring back is good,
Δ: Springback is good but the yield ratio YR is low (impact in shock absorbing performance),
X: Springback failure.

  In the material of the present invention, it was confirmed that the amount of springback was good. In addition, even if the springback is within the criterion, a material having a low yield ratio YR is inferior in impact absorbing performance, and therefore does not satisfy the target characteristics of the material of the present invention.

  For example, when the punch Rp = 10 and the plate thickness t = 1.4 mm, Rp / t = 7.1. At this time, the allowable amount of spring back is θ <6.5, and if more spring back occurs, it is difficult to reduce the spring back due to the possibility of the mold.

  The hot-rolled steel sheet according to the present invention, which is excellent in local rolling performance, has ultrafine crystal grains, has a high yield strength with a yield strength ratio (yield ratio) of 0.8 or more, and an impact. Excellent absorption characteristics and shape freezing properties. Furthermore, the hot-rolled steel sheet excellent in local rolling performance according to the present invention has thermal stability capable of withstanding the heat of the welding process and the hot dipping process, in addition to excellent shock absorption characteristics and shape freezing properties. And these hot-rolled steel plates excellent in local rolling performance can be easily manufactured by the method of the present invention.

The ultimate stress of a local bending part in the case of implementing a local bending test is shown. When a steel plate is bent, a crack is generated at the bent portion. It is an example of the shape of the bending part when carrying out the adhesion bending process of the steel plate. This is a plot of various hot-rolled steel sheets by yield ratio YR and springback amount. Sectional drawing of the local bending part periphery of the hot-rolled steel plate in local bending is shown. It is a plastic tangent gradient curve, the X axis indicates plastic strain (true strain), and the Y axis indicates stress (true stress). The above-mentioned limited range is expanded among the plastic tangent gradient curves in FIG. The data obtained from the examples are plotted with YR on the X-axis and H ′ / TS on the Y-axis. Sectional drawing of the bending part periphery of a hot-rolled steel plate in close_contact | adherence bending processing (hem processing) is shown. The stress generated in the local bending process is simulated for each local bending position. The state before and after the tension | tensile_strength of the JIS5 tension test piece for evaluating local stretch performance is shown. The strain (deformation) distribution of the micro area | region in the width direction center part of a test piece is shown. A procedure for bending the test piece 1 to 90 degrees with a V-bending mold will be described. A procedure for closely attaching the test piece 1 bent at 90 degrees will be described. The local bending test method is shown. A method for measuring the amount of springback is shown.

Explanation of symbols

DESCRIPTION OF SYMBOLS 1 Test piece 2 Punch which has V-shaped male type | mold 3 Dice which has V-shaped female type | mold 4 Upper mold | die of close_contact | adherence bending mold 5 Lower mold | type of close_contact | adherence bending mold a pad b dice c pad d Test piece

Claims (8)

A steel plate made of carbon steel or low alloy steel containing one or more of Ti, Nb, Mo, and V in total of 0.05% or less and having ferrite as a main phase, the plate from the surface of the steel plate The average grain size D (μm) of ferrite at a depth of 1/4 of the thickness satisfies the following formulas (1) and (2), the yield ratio is 0.8 or more, and JIS No. 5 tensile The average plastic tangent gradient H ′ in the range from the plastic strain after yielding 0.005 to the 65% strain of uniform elongation in the test is excellent in local elongation performance characterized by satisfying the following formula (3): Hot rolled steel sheet.
1.2 ≦ D ≦ 7 (1) Formula D ≦ 2.7 + 5000 / (5 + 350 · C + 40 · Mn) ² (2) Formula 0.1 ≦ H ′ / TS ≦ −2 × YR + 3.1 (3) Formula where D is 1/4 of the plate thickness from the steel plate surface. The average crystal grain size (μm) of ferrite at the depth position, C and Mn are the contents (mass%) of each element in the steel, and H ′ is uniform from the plastic strain after yield of 0.005 in the tensile test. The average plastic tangent gradient in the range up to 65% strain of elongation, TS is the tensile strength (MPa), and YR is the yield ratio. The average crystal grain diameter D _s (μm) of ferrite on the steel sheet surface layer and the average crystal grain diameter D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface satisfy the following formula (4): The hot-rolled steel sheet having excellent local rolling performance according to claim 1.
D _s /D≦0.8 (4) where D _s is the average crystal grain size (μm) of ferrite on the steel sheet surface layer, and D represents the average crystal grain size (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel plate surface. The ferrite crystal grain size d (μm) satisfying the following formula (5) at the depth position of 1/4 of the plate thickness from the steel plate surface, the area ratio of the ferrite crystal grains to the ferrite is 80% or more. The hot-rolled steel sheet excellent in local rolling performance according to claim 1 or 2.
D / 3 ≦ d ≦ 3D (5) where d is the ferrite crystal grain size (μm) and D is the surface of the steel plate. The average crystal grain size (μm) of ferrite at a depth position of ¼ of the thickness is shown. The increase rate X (μm / min) at 700 ° C. of the average crystal grain size D (μm) of ferrite at a depth position of ¼ of the plate thickness from the steel sheet surface and the average crystal grain size D (μm) are as follows ( The hot-rolled steel sheet having excellent local rolling performance according to any one of claims 1 to 3, wherein the formula (6) is satisfied.
Here D · X ≦ 0.1 ················ (6) formula, D is the average from the steel sheet surface of the ferrite in the 1/4 depth position of the sheet thickness crystal The particle size (μm) and X represents the rate of increase (μm / min) at 700 ° C. of the average crystal particle size D (μm) of the ferrite.   The surface of a hot-rolled steel sheet excellent in local rolling performance according to any one of claims 1 to 4, comprising a coating layer of Zn, Al, Zn-Al alloy or Fe-Zn alloy, Hot-dip hot-rolled steel sheet with excellent local rolling performance. A method of producing a hot-rolled steel sheet excellent in local rolling performance by multi-pass hot rolling a slab made of carbon steel or low-alloy steel, wherein the final rolling pass is at a temperature of Ar ₃ points or higher and 780 ° C. or higher. And then cooled to 720 ° C. or less within 0.4 seconds at a cooling rate of 400 ° C./second or more, and then held at a temperature range of 600 to 720 ° C. for 2 seconds or more, then 0.1 to 1.0% The method for producing a hot-rolled steel sheet having excellent local rolling performance according to any one of claims 1 to 4, wherein the temper rolling is performed. A method of producing a hot-rolled steel sheet having excellent local rolling performance by multi-pass hot rolling a slab made of carbon steel or low-alloy steel, and the final rolling pass is performed at a final final stand rolling ratio of 10 to 50%. In addition, it is finished at a temperature of Ar ₃ points or more and 780 ° C. or more, and then cooled to 720 ° C. or less within 0.4 seconds at a cooling rate of 400 ° C./second or more, and then at a temperature range of 600 to 720 ° C. for 2 seconds or more. The method for producing a hot-rolled steel sheet having excellent local rolling performance according to any one of claims 1 to 4, wherein the temper rolling is performed at 0.1 to 1.0% after the holding.   A hot-rolled steel sheet excellent in local elongation performance obtained by the method according to claim 6 or 7 is subjected to hot-dip plating in a continuous hot dipping line after pickling, and has excellent local elongation performance. A method for producing a plated hot-rolled steel sheet.

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