HIGH STRENGTH STEEL SHEET, METHOD FOR PRODUCING SAME, MEMBER, AND METHOD FOR PRODUCING SAME

Description

CROSS REFERENCE TO RELATED APPLICATIONS

This is the U.S. National Phase application of PCT/JP2023/027131, filed Jul. 25, 2023, which claims priority to Japanese Patent Application No. 2022-135896, filed Aug. 29, 2022, the disclosures of these applications being incorporated herein by reference in their entireties for all purposes.

FIELD OF THE INVENTION

The invention relates to a high strength steel sheet having a yield strength (YS) of not less than 800 MPa and a method of producing the same as well as a member and a method of producing the same.

BACKGROUND OF THE INVENTION

In recent years, in the automotive industry for example, an improvement in the fuel efficiency of automobiles has been hoped for to reduce the carbon dioxide gas (CO₂) emission from a viewpoint of the preservation of the global environment.

In order to improve the fuel efficiency of automobiles, it is effective to reduce the vehicle body weight, and in this case, it is necessary to reduce the vehicle body weight while maintaining the strength of the vehicle body. If the number of automotive parts can be reduced by strengthening a steel sheet which becomes the parts and simplifying the structure of the vehicle body, reduction of the vehicle body weight can be achieved.

For example, Patent Literatures 1 to 3 each disclose a high strength steel sheet having a yield strength of not less than 800 MPa.

PATENT LITERATURE

• Patent Literature 1: JP 2018-21231 A
• Patent Literature 2: JP 2018-21233 A
• Patent Literature 3: JP 2017-214647 A

SUMMARY OF THE INVENTION

To form a high strength steel sheet having a yield strength of not less than 800 MPa into automotive parts, good workability is required.

Further, a steel sheet used as automotive parts is also required to be excellent in terms of proof stress at a collision (hereinafter, referred to as “collision proof stress”) and to suppress the growth of a crack generated due to an external force at a collision (i.e., to have an excellent crack stopping property).

Therefore, aspects of the present invention aim at providing a high strength steel sheet having a yield strength of not less than 800 MPa and also having excellent workability, collision proof stress, and crack stopping property.

The present inventors found that employing the configuration described below enables the achievement of the above-mentioned object. Aspects of the present invention have been thus completed.

Specifically, aspects of the present invention include the following [1] to [10].

[1] A high strength steel sheet comprising a steel sheet,

• • wherein an amount of diffusible hydrogen in steel of the steel sheet is not more than 0.50 mass ppm,
  • the steel sheet has chemical composition and microstructure,
  • the chemical composition including, by mass,
  • C in an amount of 0.150 to 0.500%,
  • Si in an amount of 0.01 to 3.00%,
  • Mn in an amount of 1.50 to 4.00%,
  • P in an amount of not more than 0.100%,
  • S in an amount of not more than 0.0200%,
  • Al in an amount of not more than 0.100%,
  • N in an amount of not more than 0.0100%, and
  • O in an amount of not more than 0.0100%, with a balance being Fe and inevitable impurities,
  • in the microstructure,
  • a total area fraction of tempered martensite and bainite is 55 to 95%,
  • a presence ratio A/B of a structure A to a structure B is 0.8 to 2.5, the structure A having a nanohardness of 7 GPa or more, and the structure B having a nanohardness of 6 GPa or less, and
  • a concentration of solid solution carbon in retained austenite is 0.50 to 0.90 mass %.
    [2] The high strength steel sheet according to [1] above,
  • wherein the chemical composition further includes at least one element selected from the group consisting of, by mass,
  • B in an amount of not more than 0.0100%,
  • Ti in an amount of not more than 0.200%,
  • Nb in an amount of not more than 0.200%,
  • V in an amount of not more than 0.200%,
  • W in an amount of not more than 0.100%,
  • Mo in an amount of not more than 1.000%,
  • Cr in an amount of not more than 1.000%,
  • Sb in an amount of not more than 0.200%,
  • Sn in an amount of not more than 0.200%,
  • Zr in an amount of not more than 0.1000%,
  • Te in an amount of not more than 0.100%,
  • Cu in an amount of not more than 1.000%,
  • Ni in an amount of not more than 1.000%,
  • Ca in an amount of not more than 0.0100%,
  • Mg in an amount of not more than 0.0100%,
  • REM in an amount of not more than 0.0100%,
  • Co in an amount of not more than 0.010%,
  • Ta in an amount of not more than 0.10%,
  • Hf in an amount of not more than 0.10%, and
  • Bi: in an amount of not more than 0.200%.
    [3] The high strength steel sheet according to [1] or [2] above,
  • wherein a plating layer is further provided on a surface of a steel sheet.
    [4] The high strength steel sheet according to [3] above,
  • wherein the plating layer is a galvanizing layer, a galvannealing layer, or an electrogalvanizing layer.
    [5] A method of producing the high strength steel sheet according to [1] above, the method comprising:
  • subjecting a steel slab having the chemical composition according to [1] above to hot rolling to obtain a hot rolled steel sheet;
  • subjecting the hot rolled steel sheet to cold rolling to obtain a cold rolled steel sheet; and
  • heating the cold rolled steel sheet at a heating temperature T1 of 750° C. to 950° C. for 10 s to 500 s, cooling the heated cold rolled steel sheet to a cooling stop temperature T2 of not lower than 120° C. and lower than 280° C., re-heating the cooled cold rolled steel sheet to a re-heating temperature T3, re-cooling the re-heated cold rolled steel sheet without retaining the re-heated cold rolled steel sheet at the re-heating temperature T3, and retaining the re-cooled cold rolled steel sheet at a temperature T4 lower than the re-heating temperature T3 for 1 s or more,
  • wherein a heat-input effect index J from the cooling stop temperature T2 to the re-heating temperature T3, as expressed by Formula (1) below, is 1500 to 4000, and
  • the cold rolled steel sheet retained at the temperature T4 is subjected to temper rolling using a roll having a surface roughness of 1.5 to 5.0 μm,

J = ( T ⁢ 3 - T ⁢ 2 ) ⁢ ( log ⁡ ( 9 ⁢ t )   +   20 ) ( 1 )

• • in Formula (1), t is a heating time from the cooling stop temperature T2 to the re-heating temperature T3 ° C., and a unit of the heating time is s.
    [6] A method of producing the high strength steel sheet according to [2] above, the method comprising:
  • subjecting a steel slab having the chemical composition according to [2] above to hot rolling to obtain a hot rolled steel sheet;
  • subjecting the hot rolled steel sheet to cold rolling to obtain a cold rolled steel sheet; and
  • heating the cold rolled steel sheet at a heating temperature T1 of 750° C. to 950° C. for 10 s to 500 s, cooling the heated cold rolled steel sheet to a cooling stop temperature T2 of not lower than 120° C. and lower than 280° C., re-heating the cooled cold rolled steel sheet to a re-heating temperature T3, re-cooling the re-heated cold rolled steel sheet without retaining the re-heated cold rolled steel sheet at the re-heating temperature T3, and retaining the re-cooled cold rolled steel sheet at a temperature T4 lower than the re-heating temperature T3 for 1 s or more,
  • wherein a heat-input effect index J from the cooling stop temperature T2 to the re-heating temperature T3, as expressed by Formula (1) below, is 1500 to 4000, and
  • the cold rolled steel sheet retained at the temperature T4 is subjected to temper rolling using a roll having a surface roughness of 1.5 to 5.0 μm,

J = ( T ⁢ 3 - T ⁢ 2 ) ⁢ ( log ⁡ ( 9 ⁢ t )   +   20 ) ( 1 )

• • in Formula (1), t is a heating time from the cooling stop temperature T2 to the re-heating temperature T3° C., and a unit of the heating time is s.
    [7] The method of producing the high strength steel sheet according to [5] or [6] above,
  • wherein the cold rolled steel sheet is subjected to a plating treatment.
    [8] The method of producing the high strength steel sheet according to [7] above,
  • wherein the plating treatment is a galvanizing treatment, a galvannealing treatment, or an electrogalvanizing treatment.
    [9] A member obtained by using the high strength steel sheet according to any one of [1] to [4] above.
    [10] A method of producing a member, the method comprising subjecting the high strength steel sheet according to any one of [1] to [4] above to at least one of a forming process and a joining process to obtain a member.

Aspects of the present invention can provide a high strength steel sheet having a yield strength of not less than 800 MPa and also having excellent workability, collision proof stress, and crack stopping property.

BRIEF DESCRIPTION OF THE DRAWINGS

FIG. 1 is a chart diagram showing one example of a heat treatment.

FIG. 2A is a cross-sectional view showing a hat member.

FIG. 2B is a schematic view showing the hat member subjected to a three-point bending test.

DETAILED DESCRIPTION OF EMBODIMENTS OF THE INVENTION

[High Strength Steel Sheet]

A high strength steel sheet of the present embodiment (hereinafter also referred to as the “present high strength steel sheet”) includes a steel sheet, and may further include a plating layer on a surface of the steel sheet as described later.

The steel sheet included in the present high strength steel sheet has the chemical composition and microstructure which are to be described later, and satisfies the amount of diffusible hydrogen in steel to be described later.

The term “high strength” means having a yield strength (YS) of not less than 800 MPa.

The present high strength steel sheet has a yield strength of not less than 800 MPa and also has excellent workability, collision proof stress, and crack stopping property. Therefore, since the strength against a collision is sufficient, the present high strength steel sheet is suitably used as parts of transportation machines such as automobiles.

As a method of forming the present high strength steel sheet, a general processing method such as press working can be used without limitation. As a method of welding the present high strength steel sheet, a general welding method such as spot welding or arc welding can be used without limitation.

<Steel Sheet>

First, the steel sheet included in the present high strength steel sheet is described.

The thickness of the steel sheet is not particularly limited and is, for example, not less than 0.5 mm and not more than 3.0 mm.

<<Chemical Composition>>

Chemical composition of the steel sheet included in the present high strength steel sheet (hereinafter, conveniently referred to as “present chemical composition”) is described. The percentage “%” used in the present chemical composition means “mass %” unless otherwise noted.

(C: 0.150 to 0.500%)

C generates martensite to raise the strength of the steel sheet. When the amount of C is too small, the total area fraction of tempered martensite and bainite decreases, whereby the collision proof stress and the yield strength deteriorate. Hence, the amount of C is not less than 0.150%, preferably not less than 0.180%, and more preferably not less than 0.200%.

Meanwhile, an excessively large amount of C leads to an increase in a structure A having a nanohardness of 7 GPa or more which becomes a starting point of cracking, resulting in lower workability. Hence, the amount of C is not more than 0.500%, preferably not more than 0.460%, and more preferably not more than 0.400%.

(Si: 0.01 to 3.00%)

Si suppresses generation of carbides during a heat treatment and influences the hardness of a structure and the concentration of solid solution carbon in retained austenite. From the viewpoint of ensuring a structure having suitable nanohardness and obtaining at least a certain concentration of solid solution carbon in retained austenite, the amount of Si is not less than 0.01%, preferably not less than 0.50%, and more preferably not less than 0.80%.

Meanwhile, when the amount of Si is too large, the concentration of solid solution carbon in retained austenite excessively increases. Hence, the amount of Si is not more than 3.00%, preferably not more than 2.60%, and more preferably not more than 2.40%.

(Mn: 1.50 to 4.00%)

Mn influences the area fraction of tempered martensite and bainite. From the viewpoint of obtaining a good collision proof stress and a yield strength of not less than 800 MPa, the amount of Mn is not less than 1.50%, preferably not less than 1.90%, and more preferably not less than 2.30%.

Meanwhile, an excessively large amount of Mn leads to an increase in the structure A having a nanohardness of 7 GPa or more which becomes a starting point of cracking, resulting in lower workability. Hence, the amount of Mn is not more than 4.00%, preferably not more than 3.50%, and more preferably not more than 3.30%.

(P: Not more than 0.100%)

P is segregated in a prior austenite grain boundary to embrittle the grain boundary. This reduces the ultimate deformability of the steel sheet, resulting in lower workability. Accordingly, the amount of P is not more than 0.100%, preferably not more than 0.030%, and more preferably not more than 0.010%.

While the lower limit of the amount of P is not particularly limited, since P is a solid-solution strengthening element and increases the strength of the steel sheet, the amount of P is preferably 0.001%, more preferably 0.002%, and further preferably 0.003%.

(S: Not more than 0.0200%)

S combines with Mn to form coarse MnS which becomes a starting point of cracking, resulting in lower workability. Hence, the amount of S is not more than 0.0200%, preferably not more than 0.0100%, and more preferably not more than 0.0020%.

The lower limit of the amount of S is not particularly limited and is preferably 0.0001%, more preferably 0.0002%, and further preferably 0.0003% due to production engineering restrictions.

(Al: Not more than 0.100%)

Al increases an A₃ transformation point. This leads to an increase in ferrite, and thus the total area fraction of tempered martensite and bainite decreases. Hence, the amount of Al is not more than 0.100%, preferably not more than 0.080%, and more preferably not more than 0.060%.

The lower limit of the amount of Al is not particularly limited and is, for example, 0.010% and preferably 0.020% because generation of carbides during a heat treatment is suppressed and generation of retained austenite is promoted.

(N: Not more than 0.0100%)

N combines with Ti to form TiN which becomes a starting point of cracking, resulting in lower workability. Hence, the amount of N is not more than 0.0100%, preferably not more than 0.0080%, and more preferably not more than 0.0060%.

The lower limit of the amount of N is not particularly limited and is preferably 0.0001%, more preferably 0.0003%, and further preferably 0.0005% due to production engineering restrictions.

(O: Not more than 0.0100%)

O forms an oxide which becomes a starting point of cracking, resulting in lower workability. Hence, the amount of O is not more than 0.0100%, preferably not more than 0.0050%, and more preferably not more than 0.0020%.

(Other Elements)

The present chemical composition may further include at least one element selected from the group consisting of elements described below, in percentage by mass.

((B: Not more than 0.0100%))

B is preferably added because it is an element capable of improving the hardenability of the steel sheet by being segregated in an austenite grain boundary and increases the yield strength of the steel sheet.

Meanwhile, when the amount of B is too large, Fe₂₃(CB)₆ is formed and becomes a starting point of cracking, resulting in lower workability. Hence, the amount of B is preferably not more than 0.0100%, more preferably not more than 0.0050%, further preferably not more than 0.0040%, and particularly preferably not more than 0.0030%.

The lower limit of the amount of B is not particularly limited and is, for example, 0.0005% and preferably 0.0010% from the viewpoint of obtaining the effect of addition of B.

((Ti: Not more than 0.200%))

Ti is preferably added because it forms a fine carbide, nitride, or carbonitride during hot rolling or a heat treatment to thereby increase the yield strength of the steel sheet.

However, when the amount of Ti is too large, Ti combines with N, so that thus-formed coarse nitrides which become starting points of cracking increase, resulting in lower workability. Hence, the amount of Ti is preferably not more than 0.200%, more preferably not more than 0.100%, and further preferably not more than 0.050%.

The lower limit of the amount of Ti is not particularly limited and is, for example, 0.005%, and preferably 0.010% from the viewpoint of obtaining the effect of addition of Ti.

((Nb: Not more than 0.200%, V: Not more than 0.200%, W: Not more than 0.100%))

Nb, V, and W are preferably added because they form fine carbides, nitrides, or carbonitrides during hot rolling or a heat treatment to thereby increase the yield strength of the steel sheet.

However, when the amounts to add are excessively large, these elements do not dissolve during steel slab heating and remain as coarse carbides. The coarse carbides become starting points of cracking at a collision, resulting in lower workability. Hence, the amount of Nb is preferably not more than 0.200%, more preferably not more than 0.100%, and further preferably not more than 0.050%. The lower limit thereof is not particularly limited and is, for example, 0.005% and is preferably 0.010% from the viewpoint of obtaining the effect of addition of Nb.

The amount of V is preferably not more than 0.200%, more preferably not more than 0.100%, and further preferably not more than 0.050%. The lower limit thereof is not particularly limited and is, for example, 0.005% and preferably 0.010% from the viewpoint of obtaining the effect of addition of V.

The amount of W is preferably not more than 0.100%, more preferably not more than 0.080%, and further preferably not more than 0.050%. The lower limit thereof is not particularly limited and is, for example, 0.010% and preferably 0.020% from the viewpoint of obtaining the effect of addition of W.

((Mo: Not more than 1.000%, Cr: Not more than 1.000%))

Mo and Cr are preferably added because they increase the hardenability of the steel sheet to thereby increase the yield strength of the steel sheet. However, when the amounts of these elements are excessively large, hard martensite is excessively generated so that a starting point of cracking increases, resulting in lower workability.

Hence, the amount of Mo is preferably not more than 1.000%, more preferably not more than 0.800%, and further preferably not more than 0.500%. The lower limit thereof is not particularly limited and is, for example, 0.010% and preferably 0.020% from the viewpoint of obtaining the effect of addition of Mo.

The amount of Cr is preferably not more than 1.000%, more preferably not more than 0.800%, and further preferably not more than 0.500%. The lower limit thereof is not particularly limited and is, for example, 0.010% and preferably 0.020% from the viewpoint of obtaining the effect of addition of Cr.

((Sb: Not more than 0.200%, Sn: Not more than 0.200%))

Sb and Sn are preferably added because they suppress decarburization of the surfaces of the steel sheet to thereby increase the yield strength of the steel sheet. However, when the amounts of these elements are excessively large, the steel is embrittled, resulting in lower workability.

Hence, the amount of Sb is preferably not more than 0.200%, more preferably not more than 0.080%, and further preferably not more than 0.040%. The lower limit thereof is not particularly limited and is, for example, 0.001% and preferably 0.002% from the viewpoint of obtaining the effect of addition of Sb.

The amount of Sn is preferably not more than 0.200%, more preferably not more than 0.080%, and further preferably not more than 0.040%. The lower limit thereof is not particularly limited and is, for example, 0.001% and preferably 0.002% from the viewpoint of obtaining the effect of addition of Sn.

((Zr: Not more than 0.1000%, Te: Not more than 0.100%))

Zr and Te are preferably added because they spheroidize the shapes of nitrides and sulfides to thereby improve workability. However, when the amounts of these elements are excessively large, coarse precipitates remaining in an undissolved state increase during steel slab heating in hot rolling, thus degrading workability.

Hence, the amount of Zr is preferably not more than 0.1000%, more preferably not more than 0.0800%, and further preferably not more than 0.0500%. The lower limit thereof is not particularly limited and is, for example, 0.0050% and preferably 0.0100% from the viewpoint of obtaining the effect of addition of Zr.

The amount of Te is preferably not more than 0.100%, more preferably not more than 0.080%, and further preferably not more than 0.050%. The lower limit thereof is not particularly limited and is, for example, 0.005% and preferably 0.010% from the viewpoint of obtaining the effect of addition of Te.

((Cu: Not more than 1.000%))

Cu is preferably added because it increases the hardenability of the steel sheet to thereby increase the yield strength of the steel sheet. However, when the amount of Cu is excessively large, inclusions of Cu increase, thus degrading workability.

Hence, the amount of Cu is preferably not more than 1.000%, more preferably not more than 0.800%, and further preferably not more than 0.500%. The lower limit thereof is not particularly limited and is, for example, 0.010% and preferably 0.020% from the viewpoint of obtaining the effect of addition of Cu.

((Ni: Not more than 1.000%))

Ni is preferably added because it increases the hardenability of the steel sheet to thereby increase the yield strength of the steel sheet. However, when the amount of Ni is excessively large, hard martensite increases, thus degrading workability.

Hence, the amount of Ni is preferably not more than 1.000%, more preferably not more than 0.800%, and further preferably not more than 0.500%. The lower limit thereof is not particularly limited and is, for example, 0.010% and preferably 0.020% from the viewpoint of obtaining the effect of addition of Ni.

((Ca: Not more than 0.0100%, Mg: Not more than 0.0100%, REM: Not more than 0.0100%))

Ca, Mg, and REM (Rare Earth Metal) are preferably added because they spheroidize the shapes of precipitates such as sulfides and oxides, thus improving workability. However, when the amounts of these elements are excessively large, coarse sulfides become starting points of cracking at a collision, thus degrading workability.

Hence, the amount of Ca is preferably not more than 0.0100%, more preferably not more than 0.0050%, and further preferably not more than 0.0040%. The lower limit thereof is not particularly limited and is, for example, 0.0005% and preferably 0.0010% from the viewpoint of obtaining the effect of addition of Ca.

The amount of Mg is preferably not more than 0.0100%, more preferably not more than 0.0050%, and further preferably not more than 0.0040%. The lower limit thereof is not particularly limited and is, for example, 0.0005% and preferably 0.0010% from the viewpoint of obtaining the effect of addition of Mg.

The amount of REM is preferably not more than 0.0100%, more preferably not more than 0.0040%, and further preferably not more than 0.0030%. The lower limit thereof is not particularly limited and is, for example, 0.0005% and preferably 0.0010% from the viewpoint of obtaining the effect of addition of REM.

((Co: Not more than 0.010%, Ta: Not more than 0.10%, Hf: Not more than 0.10%, Bi: Not more than 0.200%))

Co, Ta, Hf, and Bi are preferably added because they spheroidize the shapes of precipitates to thereby improve workability. However, when the amounts of these elements are excessively large, coarse precipitates become starting points of cracking, thus degrading workability.

Hence, the amount of Co is preferably not more than 0.010%, more preferably not more than 0.008%, and further preferably not more than 0.007%. The lower limit thereof is not particularly limited and is, for example, 0.001% and preferably 0.002% from the viewpoint of obtaining the effect of addition of Co.

The amount of Ta is preferably not more than 0.10%, more preferably not more than 0.08%, and further preferably not more than 0.07%. The lower limit thereof is not particularly limited and is, for example, 0.01% and preferably 0.02% from the viewpoint of obtaining the effect of addition of Ta.

The amount of Hf is preferably not more than 0.10%, more preferably not more than 0.08%, and further preferably not more than 0.07%. The lower limit thereof is not particularly limited and is, for example, 0.01% and preferably 0.02% from the viewpoint of obtaining the effect of addition of Hf.

The amount of Bi is preferably not more than 0.200%, more preferably not more than 0.100%, and further preferably not more than 0.080%. The lower limit thereof is not particularly limited and is, for example, 0.001% and preferably 0.005% from the viewpoint of obtaining the effect of addition of REM.

(Balance)

The balance in the present chemical composition consists of Fe and inevitable impurities.

<<Microstructure>>

Next, the microstructure of the steel sheet included in the present high strength steel sheet (hereinafter, conveniently referred to as “present microstructure”) is described.

In order to obtain the effect according to aspects of the present invention, it is not enough to satisfy the present chemical composition alone, and it is necessary to satisfy the present microstructure described below.

Hereinbelow, the area fraction is an area fraction with respect to the entire microstructure. The area fraction of each structure is determined by a method described in Examples below.

(Total area fraction of tempered martensite and bainite: 55% to 95%)

From the viewpoint of stably securing good collision proof stress and yield strength, the total area fraction of tempered martensite and bainite is not less than 55%, preferably not less than 58%, and more preferably not less than 60%.

Meanwhile, when the total area fraction of tempered martensite and bainite is too large, the structure A having a nanohardness of 7 GPa or more increases, and a presence ratio of the structure A to a structure B (A/B) becomes excessively high, thus degrading workability.

Accordingly, this total area fraction is not more than 95%, preferably not more than 92%, and more preferably not more than 88%.

(Presence ratio A/B:0.8 to 2.5)

The structure A having a nanohardness of 7 GPa or more is fine and hard, and hence stops the growth of a crack generated due to an external force at a collision, thus improving a crack stopping property.

The structure B having a nanohardness of 6 GPa or less has high toughness and thus improves workability.

When the presence ratio of the structure A to the structure B (A/B) is appropriately controlled, the crack stopping property and the workability are both excellent.

The presence ratio (A/B) is not less than 0.8, preferably not less than 1.0, and more preferably not less than 1.1 for the reason that the crack stopping property is excellent.

Meanwhile, when the presence ratio of the structure A to the structure B (A/B) is too high, the structure A having a nanohardness of 7 GPa or more becomes a starting point of cracking, thus degrading workability. Hence, the presence ratio (A/B) is not more than 2.5, preferably not more than 2.3, and more preferably not more than 2.0.

The nanohardness is the hardness measured using a nanoindentation method and specifically is determined by a method described in Examples to be described later.

A plastic deformation resistance in a local region of a structure at a submicron level cannot be evaluated by use of other hardnesses (for instance, Vickers hardness) than the nanohardness.

(Concentration of solid solution carbon in retained austenite: 0.50 to 0.90 mass %)

The present microstructure contains retained austenite.

When the concentration of solid solution carbon in retained austenite is too high and when a stress is repeatedly applied, the hardness of martensite transformed from the retained austenite greatly increases, and this results in an increase in starting points of cracking, thus degrading workability.

Hence, the concentration of solid solution carbon in retained austenite is not more than 0.90 mass %, preferably not more than 0.85 mass %, and more preferably 0.80 mass %.

Meanwhile, when the concentration of solid solution carbon in retained austenite is too low, the workability decreases.

Hence, the concentration of solid solution carbon in retained austenite is not less than 0.50 mass %, preferably not less than 0.60 mass %, and more preferably not less than 0.70 mass %.

(Remaining Structure)

The present microstructure may include a structure (remaining structure) other than tempered martensite, bainite and retained austenite.

Examples of the remaining structure include known structures such as fresh martensite; pearlite; ferrite; iron-based carbonitride; alloyed carbonitride; and inclusions such as MnS and Al₂O₃.

The area fraction of the remaining structure is preferably not more than 20%, more preferably not more than 10%, and further preferably not more than 5%. When the area fraction of the remaining structure falls within this range, the effect according to aspects of the present invention would not be impaired.

<<Amount of Diffusible Hydrogen in Steel: Not More than 0.50 Mass Ppm>>

When the amount of diffusible hydrogen in steel is too large, delayed fracture occurs, thus degrading workability. Hence, the amount of diffusible hydrogen in steel is not more than 0.50 mass ppm, preferably not more than 0.30 mass ppm, and more preferably not more than 0.20 mass ppm.

The amount of diffusible hydrogen in steel is determined by a method described in Examples to be described later.

<Plating Layer>

The present high strength steel sheet may further have a plating layer on a surface of the steel sheet for the purpose of improving corrosion resistance and other properties.

Examples of the plating layer include a galvanizing layer, a galvannealing layer and an electrogalvanizing layer. The plating layer is formed by a plating treatment to be described later.

[Method of Producing High Strength Steel Sheet]

Next, a method of producing a high strength steel sheet according to the present embodiment (hereinafter also referred to as “present production method”) is described. The present production method is a method of producing the present high strength steel sheet described above.

The temperature at which a steel slab, the steel sheet, or the like is heated or cooled, which is described below, means a surface temperature of the steel slab, the steel sheet, or the like, unless otherwise specified.

A method of producing molten steel which becomes a steel slab (steel material) is not particularly limited, and known methods using a converter, an electric furnace, or the like are applicable. It is preferable to obtain a steel slab from molten steel by a continuous casting method. Another method such as an ingot casting blooming method or a thin slab continuous casting method may be adopted to obtain a steel slab.

<Hot Rolling>

In the present production method, first, a steel slab having the present chemical composition described above is hot-rolled. Thus, a hot rolled steel sheet is obtained.

When the hot rolling is performed, the steel slab may be re-heated in a heating furnace and then rolled. When the steel slab maintains a temperature equal to or higher than a predetermined temperature, the steel slab may be directly rolled without being heated.

In the hot rolling, the steel slab is subjected to rough rolling and finish rolling.

Preferably, the steel slab is heated to dissolve carbides in the steel slab prior to the rough rolling.

From the viewpoint of dissolving carbides or preventing an increase in rolling load, the temperature at the time of heating the steel slab (steel slab heating temperature) is preferably not lower than 1100° C. and more preferably not lower than 1150° C.

On the other hand, from the viewpoint of preventing an increase in scale loss, the steel slab heating temperature is preferably not higher than 1300° C. and more preferably not higher than 1280° C.

As described above, when the steel slab before the rough rolling maintains a temperature equal to or higher than a predetermined temperature and carbides in the steel slab are dissolved, heating of the steel slab before the rough rolling can be omitted.

The conditions of the rough rolling and the finish rolling are not particularly limited, and for example, a finish rolling end temperature is preferably 700° C. to 1100° C., and more preferably 800° C. to 1000° C.

<Cold Rolling>

Next, the hot rolled steel sheet is subjected to cold rolling to obtain a cold rolled steel sheet.

A rolling rate of the cold rolling is preferably not less than 30% and more preferably not less than 35%. The upper limit thereof is not particularly limited and is, for example, not more than 70% and preferably not more than 65%.

<Heat Treatment>

Next, the cold rolled steel sheet obtained by the cold rolling is subjected to a heat treatment.

FIG. 1 is a chart diagram showing an example of the heat treatment.

In the heat treatment, in short, the cold rolled steel sheet is heated at a heating temperature T1, cooled to a cooling stop temperature T2, then re-heated to a re-heating temperature T3, and re-cooled without being retained at the re-heating temperature T3. In the re-cooling, the cold rolled steel sheet is retained at a temperature T4 lower than the re-heating temperature T3.

The cold rolled steel sheet having undergone the heat treatment and then temper rolling, which will be described later, corresponds to the steel sheet included in the present high strength steel sheet described above.

<<Heating Temperature T1: 750° C. To 950° C., Heating Time t₁: 10 to 500 s>>

First, the cold rolled steel sheet is heated at the heating temperature T1.

At this time, when the heating temperature T1 is too low or when a heating time t₁ (the time for retaining the cold rolled steel sheet at the heating temperature T1) is too short, the steel sheet is heated in a dual phase region of ferrite and austenite. In this case, the final microstructure contains ferrite, so that the total area fraction of tempered martensite and bainite decreases.

Hence, the heating temperature T1 is not lower than 750° C., preferably not lower than 800° C., and more preferably not lower than 850° C. The heating time t₁ is not less than 10 s, preferably not less than 50 s, and more preferably not less than 80 s.

Meanwhile, when the heating temperature T1 is too high or when the heating time t₁ is too long, the amount of hydrogen entering steel increases due to an increase in hydrogen partial pressure, whereby the amount of diffusible hydrogen in steel increases.

In addition, the total area fraction of tempered martensite and bainite increases, and this leads to an excessively high presence ratio (A/B), thus degrading workability.

Hence, the heating temperature T1 is not higher than 950° C., preferably not higher than 930° C., and more preferably not higher than 900° C. The heating time t₁ is not more than 500 s, preferably not more than 300 s, and more preferably not more than 200 s.

<<Cooling Stop Temperature T2: Not Lower than 120° C. And Lower than 280° C.>>

Next, the cold rolled steel sheet having been heated at the heating temperature T1 is cooled to the cooling stop temperature T2.

When the cooling stop temperature T2 is too low, the total area fraction of tempered martensite and bainite increases, and this leads to an excessively high presence ratio (A/B), thus degrading workability.

Hence, the cooling stop temperature T2 is not lower than 120° C., preferably not lower than 140° C., and more preferably not lower than 150° C.

Meanwhile, when the cooling stop temperature T2 is too high, the total area fraction of tempered martensite and bainite decreases. In addition, the structure B having a nanohardness of 6 GPa or less increases, and this leads to an excessively low presence ratio (A/B), resulting in a poorer crack stopping property.

Hence, the cooling stop temperature T2 is less than 280° C., preferably not higher than 270° C., and more preferably not higher than 260° C.

<<Re-Heating Temperature T3>>

Next, the cold rolled steel sheet having been cooled to the cooling stop temperature T2 is re-heated to the re-heating temperature T3 and is re-cooled without being retained at the re-heating temperature T3.

The re-heating temperature T3 is not particularly limited as long as it satisfies a heat-input effect index J to be described later.

The re-heating temperature T3 is for instance not lower than 280° C., preferably not lower than 290° C., and more preferably not lower than 300° C.

On the other hand, the re-heating temperature T3 is for instance not higher than 400° C., preferably not higher than 380° C., and more preferably not higher than 350° C.

<<Heat-Input Effect Index J: 1500 to 4000>>

The heat-input effect index J from the cooling stop temperature T2 to the re-heating temperature T3 with respect to the cold rolled steel sheet is expressed by Formula (1):

J = ( T ⁢ 3 - T ⁢ 2 ) ⁢ ( log ⁡ ( 9 ⁢ t ) + 20 ) ( 1 )

In Formula (1) above, t is a heating time (unit: s) from the cooling stop temperature T2 to the re-heating temperature T3° C.

The nanohardnesses of the structures composing the microstructure change depending on the state of presence of carbon in those structures. The heat-input effect index J influences not only the state of presence of carbon but also the speed of diffusion of carbon and the place where carbon is present.

When the heat-input effect index J is too low, carbon in a structure is present in a solid solution state; consequently, the structure A having a nanohardness of 7 GPa or more increases, and this leads to an excessively high presence ratio (A/B), thus degrading workability. In addition, the concentration of solid solution carbon in retained austenite becomes excessively high, thus degrading workability.

Hence, the heat-input effect index J is not lower than 1500, preferably not lower than 1800, and more preferably not lower than 2000.

Meanwhile, when the heat-input effect index J is too high, carbon in a structure is present as a carbide; consequently, the structure B having a nanohardness of 6 GPa or less increases, and this leads to an excessively low presence ratio (A/B), resulting in a poorer crack stopping property. In addition, the concentration of solid solution carbon in retained austenite becomes excessively low, thus degrading workability.

Hence, the heat-input effect index J is not more than 4000, preferably not more than 3800, and more preferably not more than 3500.

<<Retaining Time Ta at Temperature T4 Lower than Re-Heating Temperature T3: 1 s or More>>

In the re-cooling, the cold rolled steel sheet is retained at the temperature T4 lower than the re-heating temperature T3.

The temperature T4 being not lower than the re-heating temperature T3 leads to an excessively low presence ratio (A/B), resulting in a poorer crack stopping property.

The lower limit of the temperature T4 is not particularly limited and is for instance 180° C., preferably 200° C., and more preferably 220° C.

When the cold rolled steel sheet is not retained at the temperature T4 (for example, when the retaining time t₄ at the temperature T4 is zero), the presence ratio (A/B) becomes excessively high, thus degrading workability.

Hence, the retaining time t₄ is 1 s or more, preferably 3 s or more, and more preferably 5 s or more.

<Temper Rolling>

Next, the cold rolled steel sheet having undergone the heat treatment (specifically, having been retained at the temperature T4 for 1 s or more) is subjected to temper rolling using a roll.

<<Surface Roughness of Roll: 1.5 to 5.0 μm>>

The surface roughness of a roll is controlled to adjust movable dislocation introduced in a local region at a submicron level, thus controlling the hardness distribution of a structure.

When the surface roughness of a roll is too small, the presence ratio (A/B) becomes too low, resulting in a poorer crack stopping property. Hence, the surface roughness of a roll is not less than 1.5 μm, preferably not less than 1.8 μm, and more preferably not less than 2.0 μm.

Meanwhile, when the surface roughness of a roll is too large, the presence ratio (A/B) becomes too high, thus degrading workability. Hence, the surface roughness of a roll is not more than 5.0 μm, preferably not more than 4.5 μm, and more preferably not more than 4.0 μm.

The surface roughness of a roll is an arithmetic average roughness Ra measured according to JIS B 0601.

<Plating Treatment>

In the present production method, the cold rolled steel sheet having undergone the temper rolling may be subjected to a plating treatment to form a plating layer on the surface thereof.

Examples of the plating layer include a galvanizing layer, a galvannealing layer, and an electrogalvanizing layer.

For the plating treatment, galvanizing treatment, galvannealing treatment, or electrogalvanizing treatment is preferred.

When the galvanizing treatment is performed, for example, the steel sheet is immersed in a zinc bath having a bath temperature of 440° C. to 500° C. to be galvanized. Thereafter, it is preferable to adjust a coating weight of the plating layer by gas wiping or other methods.

As the zinc bath, a zinc bath having a chemical composition including the Al content of 0.10 to 0.23 mass % with the balance being Zn and inevitable impurities is preferred.

When the galvannealing treatment is performed, an excessively low alloying temperature causes an excessively low Zn—Fe alloying rate, and this may make alloying extremely difficult. On the other hand, when the alloying temperature is too high, untransformed austenite may be transformed into pearlite. Hence, the alloying temperature is preferably 450° C. to 600° C., more preferably 470° C. to 550° C., and further preferably 470° C. to 530° C.

The electrogalvanizing treatment is performed to form an electrogalvanizing layer.

The type of the electrogalvanizing layer is not particularly limited, and known electrogalvanizing layers are advantageously applicable. The electrogalvanizing layer may be a zinc alloy plating layer obtained by adding, to Zn, one or more of such elements as Fe, Cr, Ni, Mn, Co, Sn, Pb, and Mo in suitable amounts in accordance with the intended purpose.

The coating weight of the plating layer of a galvanized steel sheet (GI), a galvannealed steel sheet (GA), or an electrogalvanized steel sheet (EG) is preferably 20 to 80 g/m² per one side (double-sided plating).

The steel sheet having undergone the plating treatment is cooled to a temperature of, for example, not higher than 50° C. The steel sheet having been cooled to a temperature of not higher than 50° C. may be subjected to rolling at an elongation rate of 0.05% to 1.00%. The elongation rate is preferably 0.08% to 0.70%.

The rolling may be performed in an apparatus that is continuous with an apparatus (plating apparatus) performing the galvanizing treatment, or may be performed in an apparatus that is discontinuous with the plating apparatus. In addition, a desired elongation rate may be achieved by one rolling operation, or a plurality of rolling operations may be performed to achieve a desired elongation rate in total.

Meanwhile, the rolling described here generally refers to temper rolling, but it may be rolling performed by processing using a leveler or the like as long as it is possible to impart an elongation rate equivalent to that achieved by temper rolling.

In the present production method, for example, the retaining temperature such as the heating temperature or the re-heating temperature need not be constant as long as it is within the above-described temperature range. A cooling rate may vary during cooling as long as it is within the above-described rate range. The heat treatment may be performed in any equipment as long as the conditions such as the above-described temperature range are satisfied.

[Member]

Next, a member of the present embodiment (hereinafter also referred to as “present member”) is described.

The present member is a member formed by using the present high strength steel sheet described above as at least part of the member, and is, for example, a member formed into a target shape by processing (e.g., pressing) the present high strength steel sheet.

The present member is preferably a member for automotive parts. Note that the member for automotive parts may include a steel sheet other than the present high strength steel sheet as a material.

As described above, the present high strength steel sheet has a yield strength of not less than 800 MPa and also has excellent workability, collision proof stress, and crack stopping property. Therefore, the present member is excellent in workability, collision proof stress, and crack stopping property and also can contribute to reduction of the vehicle body weight, and thus is suitable for all members used in, among automotive parts, particularly skeletal structure parts or reinforcing parts of automobiles.

[Method of Producing Member]

Next described is a method for producing the present member.

The present member is obtained by, for example, subjecting the present high strength steel sheet to at least one of a forming process and a joining process.

The forming process is not particularly limited, and examples thereof include press working.

The joining process is not particularly limited, and examples thereof include: general welding such as spot welding and arc welding; and crimping using rivets; and the like.

EXAMPLES

Aspects of the invention are specifically described below by way of Examples. However, the invention is not limited to the examples described below.

<Production of Steel Sheet>

Molten steel having the chemical composition as shown in Table 1 below with the balance being Fe and inevitable impurities was made in a converter, and a steel slab was obtained by a continuous casting method. In Table 1 below, the underlined figures mean those out of the ranges of the invention (the same applies to Tables 2 to 3 to be described later).

The steel slabs thus obtained were subjected to hot rolling under the conditions described in Table 2 below, and thus hot rolled steel sheets were obtained. Specifically, each steel slab was heated to 1250° C. and rough rolled, followed by finish rolling at a finish rolling end temperature of 900° C.

The hot rolled steel sheet obtained was subjected to cold rolling at a rolling rate shown in Table 2 below, thereby obtaining a cold rolled steel sheet (thickness: 1.2 mm).

The cold rolled steel sheet obtained was subjected to a heat treatment under the conditions shown in Table 2 below.

Further, the cold rolled steel sheet having undergone the heat treatment was subjected to temper rolling under the conditions shown in Table 2 below.

In some examples, both surfaces of the cold rolled steel sheet (CR) after the temper rolling were subjected to a plating treatment to obtain a galvanized steel sheet (GI), a galvannealed steel sheet (GA), or an electrogalvanized steel sheet (EG).

As a galvanizing bath, when GI was produced, a zinc bath containing Al: 0.20 mass % with the balance being Zn and inevitable impurities was used, and when GA was produced, a zinc bath containing Al: 0.14 mass % with the balance being Zn and inevitable impurities was used.

The bath temperature was 470° C. for both GI and GA production.

The coating weight of the plating layer was 45 to 72 g/m² per one side when GI was produced and 45 g/m² per one side when GA was produced.

When GA was produced, the alloying temperature was 500° C.

The composition of the plating layer of GI was the composition including Fe: 0.1 to 1.0 mass % and Al: 0.2 to 1.0 mass % with the balance being Fe and inevitable impurities. The composition of the plating layer of GA was the composition including Fe: 7 to 15 mass % and Al: 0.1 to 1.0 mass % with the balance being Fe and inevitable impurities.

When EG was produced, an electrogalvanizing treatment was performed using an electrogalvanizing line such that the resulting plating layer had a coating weight of 30 g/m² per one side.

Hereinbelow, each of the cold rolled steel sheet (CR) after the heat treatment, the galvanized steel sheet (GI), the galvannealed steel sheet (GA), and the electrogalvanized steel sheet (EG) is also simply referred to as “steel sheet.”

<Observation of Microstructure>

For each of the steel sheets thus obtained, the microstructure was observed as described below. The results are shown in Table 3 below. In Table 3 below, martensite is denoted as “M,” bainite is denoted as “B,” and austenite is denoted as “γ.”

<<Total Area Fraction of Tempered Martensite and Bainite>>

The obtained steel sheet was polished such that a cross section (L cross section) at a position of ¼ of the sheet thickness and parallel to the rolling direction became an observation surface. The observation surface was etched using 1 vol % Nital, and then enlarged and observed with a scanning electron microscope (SEM) at a magnification of 3000X.

The observation surface was observed in 10 fields, and SEM images were obtained. The obtained SEM images were analyzed to determine the total area fraction (unit: %) of tempered martensite and bainite.

More specifically, dark gray parts in each obtained SEM image were determined to be tempered martensite and bainite, and the area fraction (average area fraction of the 10 fields) was determined. For the SEM image analysis, Image-Pro available from Media Cybernetics Inc. was used as analysis software.

<<Measurement of Nanohardness>>

The obtained steel sheet was polished such that a cross section (L cross section) at a position of ¼ of the sheet thickness and parallel to the rolling direction became an observation surface. The observation surface was mirror polished with diamond paste, followed by finishing polishing with colloidal silica.

The nanohardness of the observation surface was measured at 225 points by use of a nanoindentation device having a Berkovich indenter.

The measurement conditions are set as: a loading rate and an unloading rate of 50 μN/s; a maximum load of 500 μN; a data collecting pitch of 5 ms; and a distance between dents of 2 μm or more.

Of the 225 measurement points, measurement points having a nanohardness of 7 GPa or more were specified as the structure A, while measurement points having a nanohardness of 6 GPa or less were specified as the structure B, and the ratio between the numbers of the measurement points was determined as the presence ratio (A/B) of the structure A to the structure B.

<<Measurement of Concentration of Solid Solution Carbon in Retained Austenite>>

The obtained steel sheet was ground such that a position of ¼ of the sheet thickness became an observation surface, and further polished 0.1 mm by chemical polishing.

With respect to the observation surface, peak angles of the (200) surface, (220) surface, and (311) surface of austenite were obtained using an X-ray diffraction (XRD) instrument with CoKα as an X-ray source, and a lattice constant a (unit: Å) of retained austenite was calculated by Formula (2) below.

The calculated lattice constant a of retained austenite was substituted into Formula (3) below to thereby determine the content (unit: mass %) of carbon (C) in the retained austenite, and the result was defined as the concentration of solid solution carbon in the retained austenite.

a = 1 . 7 ⁢ 9 ⁢ 021 ⁢ √ 2 / sin ⁢ θ ( 2 ) a = 3.572 + 0.0012 [ Mn ] - 0.00157 [ Si ] + 0.0056 [ Al ] + 0.033 [ C ] ( 3 )

In Formula (2), a is a lattice constant (unit: Å) of retained austenite, and θ is a value (unit: rad) obtained by dividing a diffraction peak angle of the (220) surface by 2.

In Formula (3), a is a lattice constant (unit: Å) of retained austenite, and [M] is the content (unit: mass %) of an element M in the retained austenite. It should be noted, for the content of the element M other than C, the content of each element in the chemical composition (specifically, the present chemical composition described above, for example) of the whole steel sheet is used.

<Measurement of Amount of Diffusible Hydrogen in Steel>

A specimen having a length of 30 mm and a width of 5 mm was sampled from the obtained steel sheet. For the sampled specimen, the amount of diffusible hydrogen in steel was measured by a thermal desorption analysis method. The heating rate was set to 200° C./hr. The cumulative value of the amount of hydrogen detected in the temperature range from room temperature (25° C.) to a temperature lower than 210° C. was defined as the amount of diffusible hydrogen in steel (unit: mass ppm).

The steel sheet on which the plating layer had been formed was measured in the same manner after the plating layer was removed using a router (precision grinder).

The result is shown in Table 3 below. The amount of diffusible hydrogen in steel is preferably not more than 0.50 mass ppm.

<Evaluation>

The obtained steel sheets were evaluated by the following methods. The results are shown in Table 3 below.

<<Tensile Test>>

From each of the obtained steel sheets, No. 5 specimen described in JIS Z 2241 with its longitudinal direction (tensile direction) being a direction of 90° to the rolling direction was sampled. Using the specimen thus sampled, a tensile test according to JIS Z 2241 was performed five times, and the yield strength (YS) and the elongation (El) were determined from the average value of the five times.

When the YS was not less than 800 MPa, the strength can be rated as high.

When the El was not less than 8.0%, the ductility can be rated as good, and the workability can be rated as excellent.

<<Collision Proof Stress Evaluation Test>>

Using each of the obtained steel sheets, a member (hat member) having a hat-shaped cross section was produced, and a three-point bending test was performed to determine the maximum load (unit: kN).

First, a hat member 1 is described with reference to FIG. 2A.

FIG. 2A is a cross-sectional view showing the hat member 1. In FIG. 2A, the dimensions of the hat member 1 are shown. The hat member 1 is joined to a flat plate 2 by spot welding (nugget diameter: 4.5√t, spot-to-spot pitch: 35 mm). The flat plate 2 is a cold-rolled steel sheet having no plating layer, and has a tensile strength (TS) of 590 MPa and a thickness t that is the same as that of the hat member 1 (1.2 mm).

Next, the three-point bending test is described with reference to FIG. 2B.

FIG. 2B is a schematic view showing the hat member 1 subjected to the three-point bending test. Various dimensions are shown also in FIG. 2B. The flat plate 2 joined to the hat member 1 is supported by a support member 3 which is a rigid body. In this state, an impactor 4, which is a rigid body, is moved from above toward the hat member 1 at a velocity of 1 m/s. In this way, the three-point bending test is performed.

For each steel sheet, the three-point bending test was performed three times, and the average value of the maximum loads obtained in those times was defined as the maximum load of the steel sheet.

When the maximum load was not less than 40 kN, “A” was given, when the maximum load was not less than 30 kN and less than 40 kN, “B” was given, and when the maximum load was less than 30 kN, “C” was given in Table 3 below.

When the result is A or B, the collision proof stress can be rated as excellent.

<<Crack Stopping Property Evaluation Test>>

Each of the obtained steel sheets was bent using a 90 degree V-block under the test conditions below to obtain a specimen. A ridge portion at the apex of the bend in the obtained specimen was observed with a digital microscope (RH-2000, manufactured by HIROX Co., Ltd.) at a magnification of 40X to measure the length of a crack. When plural cracks are present, the sum of the lengths of the cracks was obtained.

When the sum of the lengths of cracks was not more than 6000 μm, “A” was given, when the sum of the lengths of cracks was more than 6000 μm and less than 12000 μm, “B” was given, and when the sum of the lengths of cracks was not less than 12000 μm, “C” was given in Table 3 below.

When the result is A or B, the crack stopping property can be rated as excellent.

(Test Conditions)

• • Test method: roll supporting, punch pressing
  • Roll diameter: φ30 mm
  • Punch tip R: 0.4 mm
  • Distance between rolls: (thickness×2)+0.5 mm
  • Stroke rate: 20 mm/min
  • Specimen size: 60 mm×60 mm
  • Bending direction: Rolling perpendicular method

TABLE 1
Steel	Chemical composition [mass %]

ID	C	Si	Mn	P	S	Al	N	O	B	Ti	Nb	V	W	Mo	Cr
A	0.232	1.26	2.72	0.006	0.0005	0.035	0.0040	0.0006	0.0019	0.021	0.020	—	—	—	—
B	0.301	1.45	3.11	0.004	0.0008	0.036	0.0041	0.0007	—	—	0.019	—	—	—	—
C	0.251	1.31	2.76	0.005	0.0010	0.040	0.0039	0.0006	—	—	—	0.088	—	—	—
D	0.155	1.50	3.42	0.010	0.0010	0.052	0.0042	0.0008	—	—	—	—	0.025	—	—
E	0.288	2.92	1.52	0.009	0.0015	0.045	0.0048	0.0012	—	—	0.047	—	—	0.197	—
F	0.245	1.35	2.76	0.011	0.0011	0.042	0.0051	0.0004	0.0044	0.021	—	—	—	—	—
G	0.277	1.42	2.35	0.004	0.0007	0.031	0.0061	0.0006	—	—	—	—	—	—	—
H	0.221	1.08	1.42	0.012	0.0019	0.029	0.0035	0.0007	—	—	—	0.025	—	—	—
I	0.193	1.26	4.04	0.010	0.0020	0.041	0.0041	0.0010	—	—	0.035	—	—	—	—
J	0.503	1.25	2.23	0.006	0.0015	0.036	0.0038	0.0020	—	—	—	—	—	—	—
K	0.143	1.15	3.10	0.007	0.0012	0.055	0.0059	0.0042	—	—	—	—	—	—	—
L	0.261	1.65	2.55	0.013	0.0009	0.039	0.0035	0.0006	—	—	—	—	—	—	0.220
M	0.261	3.15	2.64	0.015	0.0015	0.032	0.0051	0.0050	—	—	—	—	—	—	—
N	0.252	0.003	2.63	0.018	0.0015	0.083	0.0034	0.0030	—	—	—	—	—	—	—
O	0.315	1.62	2.75	0.008	0.0009	0.032	0.0041	0.0004	—	—	—	—	—	—	—
P	0.242	1.36	2.62	0.006	0.0009	0.041	0.0038	0.0006	—	—	—	—	—	—	—
Q	0.265	1.31	2.83	0.009	0.0009	0.054	0.0042	0.0006	—	—	—	—	—	—	—
R	0.254	1.26	2.85	0.010	0.0009	0.042	0.0051	0.0006	—	—	—	—	—	—	—
S	0.235	1.35	2.72	0.005	0.0009	0.053	0.0034	0.0006	—	0.091	—	—	—	—	—
T	0.189	0.04	2.87	0.015	0.0016	0.029	0.0052	0.0015	—	—	—	—	—	—	—
U	0.225	2.75	2.65	0.016	0.0014	0.091	0.0041	0.0016	—	—	—	—	—	—	—
V	0.311	0.44	2.65	0.012	0.0011	0.041	0.0092	0.0004	—	—	—	—	—	—	—
W	0.238	1.26	3.55	0.010	0.0020	0.059	0.0038	0.0006	—	—	—	—	—	—	—
X	0.238	1.32	1.83	0.015	0.0016	0.049	0.0025	0.0004	—	—	—	—	—	—	—

Steel

Chemical composition [mass %]

ID	Sb	Sn	Zr	Cu	Ni	Ca	Mg	Co	Ta	REM	Hf	Te	Bi
A	—	—	—	—	—	—	—	—	—	—	—	—	—
B	0.006	—	—	—	—	—	—	—	—	—	—	—	—
C	—	—	—	—	—	—	—	—	—	—	—	—	—
D	—	—	—	—	—	—	—	—	—	—	—	—	—
E	—	—	—	—	—	—	—	—	—	—	—	—	—
F	—	—	—	0.115	—	—	—	—	—	—	—	—	—
G	—	—	—	—	—	—	—	—	—	—	—	—	—
H	—	—	—	—	—	—	—	—	—	—	—	—	—
I	—	—	—	—	—	—	—	—	—	—	—	—	—
J	—	—	—	—	—	—	—	—	—	—	—	—	—
K	—	—	—	—	—	—	—	—	—	—	—	—	—
L	0.015	—	—	—	—	—	—	—	—	—	—	—	—
M	—	—	—	—	—	—	—	—	—	—	—	—	—
N	—	—	—	—	—	—	—	—	—	—	—	—	—
O	—	0.010	0.0220	—	—	—	—	—	—	—	—	—	—
P	—	—	—	0.220	0.125	—	—	—	—	—	—	—	—
Q	—	—	—	—	—	0.0012	0.0020	—	—	—	—	—	—
R	—	—	—	—	—	—	—	0.005	—	—	—	—	—
S	—	—	—	—	—	—	—	—	0.03	0.0010	—	—	—
T	—	—	—	—	—	—	—	—	—	—	0.03	0.005	—
U	—	—	—	—	—	—	—	—	—	—	—	—	—
V	—	—	—	—	—	—	—	—	—	—	—	—	—
W	—	—	—	0.360	—	—	—	—	—	—	—	—	0.013
X	—	—	—	—	—	—	—	—	—	—	—	—	0.004

	TABLE 2
	Hot rolling		Heat treatment

		Steel	Finish	Cold			Cooling	Re-
		slab	rolling	rolling	Heating	Heating	stop	heating
		heating	end	Rolling	temperature	time	temperature	temperature
	Steel	temperature	temperature	rate	T1	t1	T2	T3
No.	ID	[° C.]	[° C.]	[%]	[° C.]	[s]	[° C.]	[° C.]
1	A	1250	900	45	870	150	200	310
2	A	1250	900	46	875	130	170	300
3	A	1250	900	45	875	130	180	310
4	A	1250	900	45	875	150	200	310
5	A	1250	900	45	870	120	180	330
6	B	1250	900	50	880	120	200	370
7	B	1250	900	50	880	120	210	350
8	B	1250	900	50	880	110	180	350
9	B	1250	900	45	880	110	200	360
10	C	1250	900	45	870	100	190	330
11	C	1250	900	45	965	100	200	320
12	C	1250	900	45	740	100	200	320
13	C	1250	900	45	870	8	200	310
14	C	1250	900	45	870	520	200	320
15	D	1250	900	50	880	150	280	350
16	E	1250	900	50	880	120	200	360
17	F	1250	900	50	880	150	200	340
18	F	1250	900	50	880	150	115	295
19	F	1250	900	50	880	150	290	370
20	F	1250	900	50	880	150	220	280
21	F	1250	900	50	880	150	200	398
22	G	1250	900	50	880	150	190	330
23	G	1250	900	50	880	150	190	250
24	G	1250	900	50	880	150	190	420
25	G	1250	900	50	880	150	200	340
26	H	1250	900	45	870	110	200	320
27	I	1250	900	50	880	150	275	370
28	J	1250	900	45	870	110	200	320
29	K	1250	900	50	880	150	270	380
30	L	1250	900	50	880	150	200	330
31	M	1250	900	50	880	150	210	330
32	N	1250	900	50	880	150	210	330
33	O	1250	900	50	865	390	210	340
34	P	1250	900	45	870	100	220	310
35	Q	1250	900	50	880	150	220	330
36	R	1250	900	50	880	60	140	290
37	S	1250	900	50	880	150	200	300
38	T	1250	900	50	880	150	220	360
39	U	1250	900	45	870	100	220	300
40	V	1250	900	45	870	100	160	300
41	W	1250	900	45	870	110	200	320
42	X	1250	900	45	870	110	200	320

Heat treatment

Temper

		Heating			Heat-	rolling
		time t		Retaining	input	Roll
		from T2	Temperature	time t4	effect	surface
		to T3	T4	at T4	index	roughness	Plating
	No.	[s]	[° C.]	[s]	J	[μm]	treatment	Remarks
	1	7	300	35	2398	2.9	CR	Compatible
								steel
	2	8	300	35	2841	2.9	CR	Compatible
								steel
	3	8	300	35	2841	2.9	GA	Compatible
								steel
	4	8	305	20	2404	1.2	CR	Comparative
								steel
	5	15	315	5	3320	2.6	CR	Compatible
								steel
	6	9	350	15	3724	3.0	CR	Compatible
								steel
	7	6	355	5	3043	3.1	CR	Comparative
								steel
	8	10	340	0	3732	2.7	CR	Comparative
								steel
	9	18	350	5	3554	5.8	CR	Comparative
								steel
	10	11	328	40	3079	3.1	EG	Compatible
								steel
	11	15	310	3	2656	3.2	GA	Comparative
								steel
	12	16	312	10	2659	3.1	EG	Comparative
								steel
	13	14	280	6	2431	1.9	CR	Comparative
								steel
	14	13	280	4	2648	1.9	CR	Comparative
								steel
	15	12	340	10	1542	2.5	CR	Compatible
								steel
	16	8	350	8	3497	2.3	GI	Compatible
								steel
	17	5	335	45	3031	2.8	CR	Compatible
								steel
	18	9	280	5	3944	1.8	CR	Comparative
								steel
	19	15	360	10	1770	1.8	CR	Comparative
								steel
	20	12	270	12	1322	1.8	GA	Comparative
								steel
	21	10	350	5	4347	1.8	CR	Comparative
								steel
	22	9	315	35	3067	3.5	CR	Compatible
								steel
	23	10	248	6	1317	3.2	GA	Comparative
								steel
	24	12	400	10	5068	3.2	CR	Comparative
								steel
	25	10	330	12	3074	1.1	CR	Comparative
								steel
	26	6	310	5	2608	2.2	CR	Comparative
								steel
	27	18	350	10	2110	2.3	CR	Comparative
								steel
	28	15	305	10	2656	2.4	CR	Comparative
								steel
	29	12	340	5	2424	2.1	CR	Comparative
								steel
	30	8	310	25	2841	2.8	CR	Compatible
								steel
	31	9	310	2	2629	2.5	CR	Comparative
								steel
	32	10	320	5	2635	2.5	CR	Comparative
								steel
	33	11	330	35	2859	3.6	GA	Compatible
								steel
	34	19	300	15	2001	3.8	GA	Compatible
								steel
	35	16	320	20	2437	3.3	GA	Compatible
								steel
	36	11	270	15	3299	3.5	GA	Compatible
								steel
	37	7	280	18	2180	3.6	GI	Compatible
								steel
	38	8	340	40	3060	3.2	CR	Compatible
								steel
	39	15	280	5	1770	2.1	GI	Compatible
								steel
	40	10	290	5	3074	1.8	EG	Compatible
								steel
	41	9	310	10	2629	2.6	CR	Compatible
								steel
	42	15	310	8	2656	4.8	CR	Compatible
								steel

	TABLE 3
	Microstructure

			Concentration
	Total area		of solid	Amount of
	fraction of		solution	diffusible
	tempered	Presence	carbon in	hydrogen			Collision	Crack
	M and B	ratio	retained γ	in steel	YS	El	proof	stopping
No.	[%]	(A/B)	[mass %]	[mass ppm]	[MPa]	[%]	stress	property	Remarks
1	85	1.4	0.68	0.00	1132	11.5	A	A	Compatible
									steel
2	88	1.3	0.70	0.00	1160	11.2	A	A	Compatible
									steel
3	80	1.2	0.62	0.19	1230	10.8	A	A	Compatible
									steel
4	82	0.6	0.71	0.00	1130	11.4	A	C	Comparative
									steel
5	80	0.9	0.73	0.00	1125	11.3	B	B	Compatible
									steel
6	90	1.6	0.75	0.00	1300	11.7	A	A	Compatible
									steel
7	88	0.7	0.72	0.00	1280	11.5	A	C	Comparative
									steel
8	92	2.6	0.68	0.00	1270	7.8	A	A	Comparative
									steel
9	80	2.7	0.72	0.00	1305	7.6	A	A	Comparative
									steel
10	81	1.2	0.64	0.00	1230	10.8	A	A	Compatible
									steel
11	97	2.8	0.55	0.65	1180	7.4	A	A	Comparative
									steel
12	43	0.9	0.51	0.25	770	9.5	C	A	Comparative
									steel
13	45	0.9	0.52	0.22	780	9.6	C	A	Comparative
									steel
14	96	2.8	0.54	0.62	1170	7.5	A	A	Comparative
									steel
15	56	2.3	0.55	0.01	810	8.2	B	B	Compatible
									steel
16	60	0.9	0.56	0.01	880	8.9	B	B	Compatible
									steel
17	85	1.5	0.72	0.00	1320	11.1	A	A	Compatible
									steel
18	96	2.8	0.59	0.01	1340	6.5	A	A	Comparative
									steel
19	46	0.7	0.54	0.01	780	9.6	C	C	Comparative
									steel
20	70	2.7	0.96	0.00	1150	6.5	B	B	Comparative
									steel
21	83	0.7	0.43	0.01	1290	6.6	A	C	Comparative
									steel
22	88	1.6	0.78	0.00	1390	11.5	A	A	Compatible
									steel
23	90	2.6	0.98	0.05	1290	7.2	A	A	Comparative
									steel
24	60	0.5	0.45	0.00	830	6.5	B	C	Comparative
									steel
25	65	0.7	0.55	0.00	840	8.6	B	C	Comparative
									steel
26	52	0.9	0.60	0.01	750	9.2	C	B	Comparative
									steel
27	92	2.8	0.61	0.01	1330	5.5	A	A	Comparative
									steel
28	94	3.2	0.63	0.01	1540	4.2	A	A	Comparative
									steel
29	43	1.0	0.52	0.01	750	8.6	C	A	Comparative
									steel
30	78	1.2	0.59	0.00	1150	9.1	A	A	Compatible
									steel
31	72	1.3	0.98	0.01	1220	7.1	A	A	Comparative
									steel
32	65	0.7	0.41	0.01	820	7.3	A	C	Comparative
									steel
33	88	1.2	0.65	0.15	1250	10.8	A	A	Compatible
									steel
34	81	1.1	0.62	0.11	1260	10.6	A	A	Compatible
									steel
35	82	1.4	0.65	0.12	1320	10.5	A	A	Compatible
									steel
36	62	1	0.62	0.12	980	11.9	A	A	Compatible
									steel
37	82	1.5	0.65	0.00	1120	11.5	A	A	Compatible
									steel
38	60	1.1	0.52	0.00	1050	8.5	A	B	Compatible
									steel
39	80	1.2	0.85	0.00	1120	8.2	A	B	Compatible
									steel
40	88	0.9	0.56	0.00	1210	8.6	A	B	Compatible
									steel
41	89	1.4	0.65	0.00	1160	8.8	A	A	Compatible
									steel
42	65	0.9	0.61	0.00	850	9.2	B	B	Compatible
									steel

Summary of Evaluation Results

As shown in Tables 1 to 3 above, the steel sheets of Nos. 1 to 3, 5, 6, 10, 15 to 17, 22, 30, and 33 to 42 all had yield strengths of not less than 800 MPa and were excellent in the workability, the collision proof stress, and the crack stopping property.

In contrast, the steel sheets of Nos. 4, 7 to 9, 11 to 14, 18 to 21, 23 to 29, 31 and 32 were insufficient in at least one of the yield strength, the workability, the collision proof stress, and the crack stopping property.