KR100380751B1 - Steel plate to be precipitating TiN+MnS for welded structures, method for manufacturing the same, welding fabric made from the same - Google Patents

Abstract

The present invention relates to structural steels used in welded structures, such as construction, bridges, shipbuilding, offshore structures, steel pipes, line pipes, etc. The object of the present invention is the welding heat using a composite precipitate in the form of MnS wrapped around the TiN precipitates To improve the toughness and strength (or hardness) of the affected portion at the same time, to provide a welded structural steel material and a method of manufacturing the same, the difference between the toughness of the base material and the heat affected zone is minimized.

The present invention for achieving the above object, in the weight% C: 0.03-0.17%, Si: 0.01-0.5%, Mn: 1.0-2.5%, Ti: 0.005-0.2%, Al: 0.0005-0.1%, N: 0.008-0.030%, B: 0.0003-0.01%, W: 0.001-0.2%, P: 0.03% or less, S: 0.003-0.05%, O: 0.005% or less, 1.2≤Ti / N≤2.5, 10≤N / Satisfying B≤40, 2.5≤Al / N≤7, 6.5≤ (Ti + 2Al + 4B) / N≤14, 220≤Mn / S≤400, and are composed of the remaining Fe and other impurities, and the microstructure is 20 The technical gist of the welded structural steel having a composite precipitate of TiN + MnS composed of a composite structure of ferrite and pearlite of 탆 or less is assumed.

Description

Steel plate to be precipitating TiN + MnS for welded structures, method for manufacturing the same, welding fabric made from the same}

The present invention relates to structural steel used in welded structures, such as construction, bridges, shipbuilding, offshore structures, steel pipes, line pipes. More specifically, the present invention relates to a welded structural steel material and a method of manufacturing the same, which can simultaneously improve the toughness and strength of the weld heat affected zone by using a composite precipitate of MnS wrapped around TiN precipitate.

Recently, steel materials used in accordance with the trend of high-rise buildings, structures are being replaced by thick materials. In order to weld such thick materials, high-efficiency welding is inevitable. As a technique for welding thickened steel materials, a high-pass heat submerged welding method and an electro-welding method capable of 1-pass welding are widely used. In addition, in the field of shipbuilding and bridges, even when welding a steel plate having a plate thickness of 25 mm or more, the above-described high heat input welding method capable of one-pass welding is applied.

In general, in welding, the larger the amount of heat input, the larger the amount of welding, so that the number of welding passes decreases. Therefore, it is advantageous to enable high heat input welding in consideration of welding productivity. In other words, increasing the amount of heat input in the welding will be able to widen the range of use. The range of high heat input currently used corresponds to approximately 100-200 kJ / cm, but in order to weld more thickened steel, that is, steel with a plate thickness of 50 mm or more, it is possible to have a super heat input range of 200-500 kJ / cm.

When the heat input is applied to the steel, the heat affected zone formed during welding, particularly the heat affected zone near the fusion boundary, is heated to a temperature close to the melting point by the amount of heat input. Accordingly, since the grains of the weld heat affected zone grow and coarse, and microstructures that are vulnerable to toughness such as upper bainite and martensite are formed during the cooling process, the weld heat affected zone is the site where the toughness of the weld deteriorates most.

Therefore, in order to secure the stability of the welded structure, it is necessary to suppress the growth of the austenite grains in the weld heat affected zone and to keep it fine. As a means to solve this problem, there is disclosed a technique for delaying grain growth of the weld heat affected zone during welding by appropriately distributing an oxide or Ti-based carbonitride, which is stable at a high temperature, to steel materials. For example, Japanese Patent Application Laid-Open No. 11-140582, No. 10-298708, No. 10-298706, No. 9-194990, No. 9-324238, No. 8-60292, (S) 60-245768, (Pyeong) 5-186848, (S) 58-31065, (S) 61-79745, Journal of the Japan Welding Society, Vol. 52, No. 2, 49 and Japanese Patent Laid-Open And 64-15320.

Japanese Patent Laid-Open No. 11-140582 is a representative technique using TiN precipitates, and has a toughness of about 200J at 0 ° C when 100 J / cm of heat input (maximum heating temperature of 1400 ° C) is applied. Is about 300J). In this prior art, Ti / N is substantially managed at 4-12 so that TiN precipitates of 0.05 µm or less are 5.8 × 10 ³ pieces / mm 2 to 8.1 × 10 ⁴ pieces / mm 2, and TiN precipitates of 0.03 to 0.2 μm are 3.9 ×. The toughness of the welded portion is secured by making the ferrite fine by depositing 10 ³ pieces / mm 2 to 6.2 × 10 ⁴ pieces / mm 2.

However, according to this prior art, when the 100 kJ / cm high heat input welding is applied, the toughness of the base material and the heat affected zone is generally low (the base material: 320J, the heat affected zone: 220J at the highest impact toughness of 0 ° C), and also the base material. Since the toughness difference between the and the heat affected zone is about 100J, there is a limit in securing the reliability of the steel structure due to superheated welding of the thickened steel. In addition, as a method for securing the desired TiN precipitate, the slab is heated at a temperature of 1050 ° C. or higher and quenched and then reheated for hot rolling, thereby increasing the manufacturing cost due to two heat treatments. It is a problem.

In addition, Japanese Patent Application Laid-Open No. 9-194990 manages the ratio of Al and O to 0.3 ≦ Al / O ≦ 1.5 in low nitrogen steel (N ≦ 0.005%) to form Al, Mn, and Si. However, the toughness is not good as the transition temperature of the welding heat affected zone is -50 level when the technique using the high heat input welding of about 100 kJ / cm is applied. In addition, Japanese Patent Application Laid-Open No. 10-298708 discloses a technique using MgO-TiN composite precipitates, but the impact toughness of the welding heat-affected zone at 0 ° C. is 130J when a high heat input welding of about 100 kJ / cm is applied. Not good.

Until now, many techniques have been known to improve the toughness of the weld heat affected zone during high heat input welding using TiN precipitates and Al-based or MgO oxides. Has not yet been published. In particular, there are few technologies in which the toughness of the weld heat affected zone shows an equivalent level to that of the base metal.

The present invention is to improve the toughness and strength (or hardness) of the weld heat affected zone by using a composite precipitate in the form of MnS wrapped around the TiN precipitate, while the toughness of the base material and the heat affected zone minimizes the difference To provide a steel material and a method of manufacturing the same, the object is.

Welded structural steel materials of the present invention for achieving the above object, by weight% C: 0.03-0.17%, Si: 0.01-0.5%, Mn: 1.0-2.5%, Ti: 0.005-0.2%, Al: 0.0005-0.1 %, N: 0.008-0.030%, B: 0.0003-0.01%, W: 0.001-0.2%, P: 0.03% or less, S: 0.003-0.05%, O: 0.005% or less, 1.2≤Ti / N≤2.5, Satisfying 10≤N / B≤40, 2.5≤Al / N≤7, 6.5≤ (Ti + 2Al + 4B) / N≤14, 220≤Mn / S≤400, and are composed of the remaining Fe and other impurities, The microstructure is composed of a composite of ferrite and pearlite of 20 μm or less.

In addition, the manufacturing method of the welded structural steel material of this invention is C: 0.03-0.17% by weight, Si: 0.01-0.5%, Mn: 1.0-2.5%, Ti: 0.005-0.2%, Al: 0.0005-0.1% , N: 0.008-0.030%, B: 0.0003-0.01%, W: 0.001-0.2%, P: 0.03% or less, S: 0.003-0.05%, O: 0.005% or less, 1.2≤Ti / N≤2.5, 10 Steel slab that satisfies ≤N / B≤40, 2.5≤Al / N≤7, 6.5≤ (Ti + 2Al + 4B) / N≤14, 220≤Mn / S≤400 and is composed of the remaining Fe and other impurities After heating 60-180 minutes in the range of 1000-1250 ° C, hot rolling at an austenitic recrystallization station with a rolling ratio of 40% or more, and then cooling the ferrite transformation temperature to ± 10 ° C at a rate of 1 ° C / min or more. do.

In addition, in the weld structure of the present invention, the heat input welding is applied to the weld structure steel (base metal) of the present invention to generate the prior austenite of 80 μm or less in the weld heat affected zone, and then quench the weld. The microstructure of the heat-affected zone is 20 micrometers or less of ferrite having a phase fraction of 70% or more.

Hereinafter, the present invention will be described in detail.

In the present invention, the term " prior austenite " refers to austenite formed in a weld heat affected zone when high heat input welding is applied to steel materials (base materials), and is formed in a steel manufacturing process (hot rolling process). It is used for convenience to distinguish it from being austenite.

As a result of investigating the old austenite grain size on the toughness of the weld heat affected zone, the present inventors found that the toughness of the weld heat affected zone changes based on the critical old austenite grain size (about 80 µm).

Based on these studies, in the present invention,

[1] using a composite precipitate of TiN + MnS,

[2] By controlling the initial ferrite grain size of the steel to less than the critical level, the old austenite is managed to about 80 µm or less. Also,

[3] By lowering the ratio of Ti / N, it effectively precipitates BN and AlN precipitates, thereby increasing the fraction of ferrite produced in the heat affected zones of welding. Especially, it is characterized by inducing ferrite into needles or polygons effective for toughness improvement. have. [1] [2] [3] will be described in detail below.

[1] TiN + MnS precipitates

The inventors note that the growth inhibition of the austenite grains is closely related to the prevention of redissolution of TiN precipitates distributed at the boundary of the weld heat affected zone near the melting line, whereby the TiN precipitates are reconsidered as a matrix. We studied ways to delay the time. As a result of this research, the present inventors found that when TiN is distributed as a TiN + MnS composite precipitate in which MnS is properly wrapped around the TiN precipitate, even if heated to a high temperature of 1350 ° C. or more, the TiN precipitate distributed in the weld heat affected zone is known (matrix). We noticed a significant delay in restocking time. In other words, MnS that is reclaimed preferentially is concentrated around TiN, affecting TiN decomposition and reusing rate to the base metal, which effectively contributes to the suppression of austenite grain growth, and thereby significantly improves the toughness of the weld heat affected zone. It can be.

For this purpose, it is important to reduce the solubility product showing the stability of the TiN precipitate at high temperature while finely and uniformly distributing the TiN + MnS composite precipitate. The inventors have investigated the size and amount of TiN + MnS composite precipitates and their distribution according to the ratio of Ti to N (Ti / N) and the ratio of Mn / S, and found that Ti / N is 1.2 to 2.5 and Mn / S. When the ratio is 220-400, TiN + MnS composite precipitates having a size of 0.01-0.1 μm were precipitated at 1.0 × 10 ⁷ / mm 2 or more, and the intervals of the precipitates were confirmed to be 0.5 μm or less.

In this way, when the ratio of Ti / N is controlled to 2.5 or less (increasing the content of N), the solubility region showing the high temperature stability of TiN is also lowered. Increasing nitrogen content at the same Ti content causes all Ti atoms to be combined with nitrogen atoms during the cooling process to increase the amount of fine TiN precipitates, resulting in the stability of precipitates at high temperatures, such as heat affected zones. Product becomes smaller. Therefore, in a high nitrogen environment, TiN precipitates are more stable than nitrogen-containing precipitates because the amount of solid solution Ti decreases. At this time, it is important to promote aging due to the presence of solid N due to high nitrogen, so that the ratio of N / B, Al / N, V / N, and overall management of these to precipitate N as BN, AlN, VN It is to let.

[2] ferrite grain size management

According to the study of the present invention, it is important that the size of the ferrite is 20 μm or less while the microstructure of the base material is a composite structure of ferrite + pearlite in order to make the size of the austenite 80 μm. At this time, the refinement of the ferrite may be obtained by controlling the growth of the ferrite grains generated in the cooling process after hot rolling as well as the austenite grain refinement by the steel working during hot rolling. For this purpose, it was confirmed that it is very effective to properly deposit and distribute carbides (VC, WC) effective for ferrite grain growth.

[3] microstructure, welded heat affected zones

The facts of the present invention reveal that the toughness of the weld heat affected zone is not only the size of the former austenite grains when the base material is heated above 1400 ° C, but also the amount of ferrite (more than 70%) that precipitates at the old austenite grain boundaries. Size (less than 20㎛) also affects. In particular, it is important to induce the transformation of polygonal ferrite and acicular ferrite in the austenite mouth. In the present invention, AlN and BN precipitates are used for this purpose.

Hereinafter, the present invention will be described in detail by dividing the steel component and its manufacturing method.

[Welding Structural Steels]

It is preferable to make content of carbon (C) into 0.03 to 0.17%.

When the content of carbon (C) is less than 0.03%, securing strength as a structural steel is insufficient. In addition, when C exceeds 0.17%, microstructures susceptible to toughness such as upper bainite, martensite and degenerate pearlite during transformation are transformed to lower the low temperature impact toughness of structural steel, and Increasing hardness or strength results in degradation of toughness and generation of weld cracks.

The content of silicon (Si) is preferably limited to 0.01-0.5%.

If the content of silicon is less than 0.01%, the deoxidation effect of molten steel is insufficient during steelmaking and the corrosion resistance of steel is reduced. If the content is more than 0.5%, the effect is saturated, It promotes the transformation of martensite and lowers the low temperature impact toughness.

The content of manganese (Mn) is preferably limited to 1.0-2.5%.

Mn is effective in improving deoxidation, weldability, hot workability and strength in steel, and precipitates in the form of MnS around Ti-based oxides, which affects the formation of needle-shaped and polygonal ferrites, which is effective for improving the toughness of weld heat affected zones. Crazy Such Mn forms a solid solution to form a solid solution in the matrix structure to strengthen the matrix to secure the strength and toughness, for this purpose it is preferably contained 1.0% or more. However, when the content exceeds 2.5%, macro segregation and micro segregation occur depending on the segregation mechanism during steel solidification, which promotes the formation of the central segregation zone in the center of the steel sheet, thereby causing the formation of low temperature transformation structure in the center of the base metal.

The content of aluminum (Al) is preferably limited to 0.0005-0.1%.

Al is not only an element necessary as a deoxidizer, but also forms a fine AlN precipitate in steel, and also forms an oxygen and Al oxide to prevent Ti from reacting with oxygen, thereby helping Ti to form fine TiN precipitate. For this purpose, it is preferable to add more than 0.0005% of Al, but if it exceeds 0.1%, AlN is precipitated and the formation of Weidmanstatten ferrite and phase martensite, in which the remaining solid solution Al is vulnerable to toughness during cooling of the weld heat affected zone. To reduce the toughness of the high heat input welding heat affected zone.

The content of titanium (Ti) is preferably limited to 0.005-0.2%.

Ti is indispensable in the present invention because it combines with N to form fine TiN precipitates that are stable at high temperatures. It is preferable to add more than 0.005% of Ti in order to obtain such a fine TiN precipitation effect, but when it exceeds 0.2%, coarse TiN precipitates and Ti oxides are formed in molten steel, and thus it is impossible to suppress the growth of the austenite grains of the weld heat affected zone. Because it is not desirable.

The content of boron (boron, B) is preferably limited to 0.0003-0.01%.

B is a very effective element for producing polygonal ferrite at grain boundaries as well as acicular ferrite having excellent toughness in grains. B forms a BN precipitate, which hinders the growth of the old austenite grains and forms Fe carbide in the grain boundary and in the mouth to promote ferrite transformation of acicular and polygons having excellent toughness. If the content of B is less than 0.0003%, such an effect cannot be expected. If the content of B is greater than 0.01%, the hardenability increases, which may cause hardening and low temperature cracking of the weld heat affected zone.

The content of nitrogen (N) is preferably limited to 0.008-0.03%.

N is an indispensable element for forming TiN, AlN, BN, VN, NbN, etc., and it is possible to minimize the growth of the old austenite grains in the weld heat affected zone during the high heat input welding and to increase TiN, AlN, BN, VN, NbN, etc. Increase the amount of precipitates. In particular, since the TiN and AlN precipitates have a remarkable effect on the size, precipitate spacing, precipitate distribution, complex precipitation frequency with oxide, and high temperature stability of the precipitate itself, the content is preferably set at 0.008% or more. However, when the nitrogen content exceeds 0.03%, the effect is saturated, and toughness is reduced due to the increase in the amount of solid solution nitrogen distributed in the weld heat affected zone, and the toughness of the weld metal may be reduced by incorporation in the weld metal due to dilution during welding. Can be.

The content of tungsten (W) is preferably limited to 0.001-0.2%.

Tungsten is an element that uniformly precipitates in the base material as tungsten carbide (WC) after hot rolling, effectively inhibiting ferrite grain growth after ferrite transformation, and also suppressing the growth of the initial austenite grains in the heating zone of the weld heat affected zone. If the content is less than 0.001%, there is less distribution of tungsten carbide for suppressing ferrite grain growth upon cooling after hot rolling, and the effect is saturated when more than 0.2% is added.

The content of phosphorus (P) is preferably limited to 0.030% or less.

P is preferably as low as possible because it is an impurity element that promotes central segregation during rolling and hot cracking during welding. In order to improve the toughness of the base metal, the toughness of the weld heat affected zone, and to reduce the center segregation, it is recommended to manage it to 0.03% or less.

The content of sulfur (S) is preferably 0.003-0.05%.

S is an element that precipitates in the form of MnS around Ti-based oxides, which is effective for improving the toughness of weld heat affected zones and affects the formation of needle-shaped and polygonal ferrites. In this case, a low melting point compound such as FeS may be formed to promote welding high temperature cracking.

The content of oxygen (O) is preferably limited to 0.005% or less.

When oxygen exceeds 0.005%, Ti element is not preferable because Ti element is formed of Ti oxide in molten steel, and TiN precipitate is not formed. Incidentally, inclusions such as coarse Fe oxide and Al oxide are formed and adversely affect the toughness of the base metal. It is not desirable because it is crazy.

The ratio of Ti / N is preferably 1.2 to 2.5.

In the present invention, the Ti / N ratio is lowered to 2.5 or less, which has two advantages. First, it is possible to increase the amount of TiN, that is, the number of TiN precipitates. In other words, if the nitrogen content is increased at the same Ti content, all the Ti atoms dissolved in the cooling process during the playing process combine with the nitrogen atom, thereby increasing the fine TiN precipitation. Second, TiN is stable at high temperatures. That is, since the solubility product which shows the stability of the precipitate at high temperature such as the weld heat affected zone becomes smaller, the precipitate such as high nitrogen TiN is more stable than the case where the nitrogen content is low. On the other hand, if the Ti / N ratio is higher than 2.5, coarse TiN is crystallized in molten steel, which is a steelmaking process, and a uniform distribution of TiN is not obtained. Also, excess Ti remaining without precipitation as TiN remains in a solid solution to weld heat. Affects bad toughness. If the Ti / N ratio is less than 1.2, the amount of solid solution nitrogen in the base metal increases, which is detrimental to the toughness of the weld heat-oriented part.

It is preferable to make ratio of N / B into 10-40.

In the present invention, if the N / B ratio is less than 10, the precipitation amount of BN that promotes the ferrite transformation of polygons at the old austenite grain boundary during the post-weld cooling process is insufficient, and when the N / B ratio is over 40, the effect is saturated and dissolved. This is because the amount of nitrogen is increased to lower the toughness of the weld heat affected zone.

It is preferable to make Al / N ratio into 2.5-7.

In the present invention, when the Al / N ratio is less than 2.5, AlN precipitates for inducing needle-like ferrite transformation are insufficient, and the amount of solid solution nitrogen in the weld heat affected zone may increase, resulting in a weld crack, and an Al / N ratio of more than 7 In the case the effect is saturated.

It is preferable that ratio of (Ti + 2Al + 4B) / N is 6.5-14.

In the present invention, when the ratio of (Ti + 2Al + 4B) / N is less than 6.5, the growth inhibition of the austenite grain growth of the weld heat affected zone, the generation of fine polygonal ferrite at the grain boundary, the amount of solid solution nitrogen, the needle shape and the polygonal shape in the grain boundary Insufficient size and number of distribution of TiN, AlN, BN, and VN precipitates for ferrite formation and control of tissue fraction, and the effect is saturated when (Ti + 2Al + 4B) / N is more than 14 seconds. If V is added, the ratio of (Ti + 2Al + 4B + V) / N is preferably 7-17. When the ratio of (Ti + 2Al + 4B + V) / N is less than 7, the growth inhibition of the old austenite grain growth of the weld heat affected zone, the generation of fine polygonal ferrite at the grain boundary, the amount of solid solution nitrogen, the needle shape in the grain and the polygonal ferrite The size and distribution of TiN, AlN, BN, and VN precipitates are insufficient for formation and control of the tissue fraction.In the case of more than 17, the nitride formation elements are larger than the nitrogen amount necessary for the formation of fine nitrides. Night grain growth inhibition effect is not exhibited.

The Mn / S ratio is preferably limited to 220 ≦ Mn / S ≦ 400.

In the present invention, the MnS precipitate is precipitated between the TiN precipitate and the base material interface to increase the temperature for inventory or delay the time required for restocking as compared to the TiN precipitate distributed alone as it is preferentially re-used as the base material during high temperature heating. Mn / S ratio should be more than 220 to secure proper MnS + TiN composite precipitates for austenitic grain growth control in the weld heat affected zone.However, when Mn / S ratio is greater than 400, MnS precipitates surrounding TiN The size is coarsened and the effect is saturated. In addition, the hardenability of the weld heat affected zone is increased to promote the reduction of toughness, hot cracking in the weld heat affected zone and the weld metal.

In order to further improve the toughness of the steel material (base material) and the heat-affected portion formed as described above, V is further added.

The content of vanadium (V) is preferably limited to 0.01-0.2%.

V is an element that combines with N to form VN to promote ferrite formation in the weld heat affected zone, and VN precipitates alone or precipitates in TIN precipitates to promote ferrite transformation. In addition, V combines with C to form VC, which acts to inhibit ferrite grain growth after ferrite transformation. When the V content is less than 0.01%, it is difficult to obtain the ferrite transformation promoting effect in the weld heat affected zone because the VN deposition amount is small. On the other hand, exceeding 0.2% is not preferable because it causes toughness of the base metal and the weld heat affected zone (HAZ) and improves the weld hardenability, which may cause the low temperature crack of the weld.

Moreover, it is preferable to make ratio of V / N into 0.3-9. In the present invention, when the V / N ratio is less than 0.3, it is difficult to secure an appropriate number and size of VN precipitates deposited and distributed at the TiN + MnS precipitate boundary for improving the toughness of the weld heat affected zone. If the V / N ratio exceeds 9, the size of the VN precipitates deposited at the TiN + MnS precipitate boundary is coarsened, and thus the VN precipitation frequency deposited at the TiN + MnS complex precipitate boundary is reduced, which is effective for the toughness of the weld heat affected zone. Reduce ferrite phase percentage.

In the present invention, in order to further improve the mechanical properties in the steel composition as described above, one or more selected from the group of Ni, Cu, Nb, Mo, Cr is further added.

The content of nickel (Ni) is preferably limited to 0.1-3.0%.

Ni is an effective element which improves the strength and toughness of the base material by solid solution strengthening. In order to achieve this effect, the Ni content is preferably 0.1% or more, but when the content exceeds 3.0%, the hardenability is increased to reduce the toughness of the weld heat affected zone and the possibility of high temperature cracking in the weld heat affected zone and the weld metal. This is not desirable because there is.

The content of copper (Cu) is preferably limited to 0.1-1.5%.

Cu is dissolved in the base and is an effective element to secure the strength and toughness of the base material due to solid solution strengthening. To achieve this effect, Cu should be added more than 0.1%, but if the content exceeds 1.5%, it is desirable because it increases the hardenability in the weld heat affected zone and lowers the toughness and promotes high temperature crack in the weld heat affected zone and the weld metal. I can't. In particular, the Cu precipitates in the form of CuS around the Ti-based oxide together with sulfur, and thus affects the formation of needle-shaped and polygonal ferrites, which is effective for improving the toughness of the weld heat affected zone, so that the content is preferably 0.1-1.5%. Do.

In the present invention, when the Cu and Ni composite addition, the sum thereof is preferably less than 3.5%. When the total of these exceeds 3.5%, the hardenability increases, which adversely affects the weld heat affected zone toughness and weldability.

The content of niobium (Nb) is preferably limited to 0.01-0.10%.

Nb is an effective element from the viewpoint of securing the strength of the base material. For this purpose, Nb is added in an amount of 0.01% or more. However, Nb is undesirable because it causes coarse precipitation of coarse NbC, which is detrimental to the toughness of the base material.

Chromium (Cr) is preferably made 0.05 to 1.0%.

Cr increases the hardenability and also improves the strength. If the content is less than 0.05%, the strength cannot be obtained and when the content exceeds 1.0%, the base metal and the HAZ toughness deteriorate.

Molybdenum (Mo) is preferably 0.05-1.0%.

Mo is also an element that increases the hardenability and improves the strength. The content thereof is 0.05% or more for securing the strength, but the upper limit is set to 1.0% like Cr for suppressing the HAZ hardening and the welding low temperature crack.

In addition, in the present invention, one or two kinds of Ca and REM are further added to suppress the grain growth of the austenite at the time of heating.

Ca and REM form an oxide having excellent high temperature stability, thereby suppressing the growth of the austenite grains when heated in the base metal and improving the toughness of the weld heat affected zone. In addition, Ca has the effect of controlling the coarse MnS shape during steelmaking. To this end, it is preferable to add more than 0.0005% of calcium (Ca) and more than 0.005% of REM, but if Ca exceeds 0.005% of REM of more than 0.05%, large inclusions and clusters are generated to harm the cleanliness of the steel. As REM, 1 type, or 2 or more types, such as Ce, La, Y, and Hf, may be used, and any of the above effects can be obtained.

· Microstructure of steel

In the present invention, after the hot rolling, the steel microstructure is made of ferrite + pearlite, and the size of the ferrite grains is preferably 20 μm or less. The reason is that when the grain size of the ferrite is larger than 20 μm, the size of the old austenite grains in the weld heat affected zone becomes 80 μm or more during high heat input welding, which is detrimental to the weld heat affected zone toughness.

In addition, the higher the percentage of ferrite in the composite structure of ferrite + perlite, the higher the toughness and elongation of the base metal, and the ferrite is 20% or more and most preferably 70% or more.

TiN + MnS composite precipitate

According to the present invention, it is preferable that more than 1.0 × 10 ⁷ TiN + MnS composite precipitates are distributed in the size of 0.01-0.1 μm per 1 mm ² . If the precipitate size is less than 0.01㎛, it is easily re-used in the base metal during the high heat input welding, so that the effect of inhibiting austenite grain growth is insufficient, and if it exceeds 0.1㎛, the pinning (grain growth inhibition) effect on the austenite grain is small. It behaves like highly coarse nonmetallic inclusions and has a detrimental effect on mechanical properties. If the number of these fine precipitates is less than 1.0 × 10 ⁷ per 1 mm ² , it is difficult to control less than 80 μm, which is the critical austenite grain size of the weld heat-affected zone when welding more than a large heat input. Since these precipitates are more advantageous in suppressing the Ostwald ripening phenomenon in which the precipitates are coarse when uniformly distributed, it is preferable to control the interval of the TiN precipitates to 0.5 μm or less.

[Method of manufacturing welded structural steel]

Refining (Deoxidation, Degassing) Process

In general, the steel refining process consists of an out-of-furnace refining process after the first refining of the converter and the second refining of the molten steel of the converter by ladle. ). Usually deoxidation takes place between primary and secondary refining.

A feature of the present invention is that in such a deoxidation process, the dissolved oxygen is adjusted to an appropriate level or lower, and then Ti is added, so that Ti is mostly dissolved in molten steel without forming Ti as an oxide. For this purpose, it is preferable to inject and deoxidize an element having a greater deoxidizing power than Ti before adding Ti. The deoxidizing power of the deoxidizer is as follows.

Cr <Mn <Si <Ti <Al <REM <Zr <Ca ≒ Mg

The amount of dissolved oxygen is greatly influenced by the formation behavior of the oxide, and the deoxidizer having a high affinity with oxygen has a very high rate of bonding with oxygen in the molten steel. Therefore, if deoxidation is performed using an element having a greater deoxidizing power before adding Ti, it is possible to prevent Ti from forming an oxide as much as possible. Of course, before the addition of the element (Al), which has a greater deoxidizing power than Ti, by adding and deoxidizing Mn, Si and the like, which are the five major elements of steel, and then deoxidizing by adding Al, the amount of deoxidizer added is preferable.

On the other hand, floating separation of inclusions in molten steel is generally known to proceed in the following order. (Dissolution of deoxygenation element in molten steel) → (Involvement of nucleation) → (Growth of inclusions) → (Continuous growth and injury due to collisions between inclusions) → (Removal of slag from slag on molten steel surface) Since the speed of each step varies depending on the type, deoxidation using a strong deoxidation element can lower the dissolved oxygen amount more easily.

In the present invention, the amount of dissolved oxygen is added as low as possible by injecting a strong deoxidation element before the introduction of Ti, and in order to maximize the amount of Ti dissolved in molten steel, it is preferable to set it as at least 30 ppm or less. The reason for this is that when the dissolved oxygen amount exceeds 30 ppm, the oxygen in the molten steel and Ti are combined to form Ti oxide easily when Ti is added, and the amount of solid solution Ti decreases.

On the other hand, according to the 'Stoke Law' widely used in steelmaking, the higher the density of inclusions, the more difficult the inclusions are. Injuries are difficult Accordingly, since inclusions increase in the steel, the addition of a deoxidation element forming a high density inclusion may be utilized as an additional advantage according to the distribution of oxides. It does not affect the effect of.

After adjusting the amount of dissolved oxygen according to the present invention, it is preferable to add Ti within 10 minutes so that the content is 0.005-0.2%. If less than 0.005% of Ti is contained in the molten steel after deoxidation, it is difficult to form a large amount of fine TiN in the casting process, and if it contains more than 0.2%, the effect is saturated and the TiN is coarsened to expect the austenite grain suppression effect. Difficult to do The reason for adding Ti within 10 minutes is that Ti oxide is generated and the amount of solid solution Ti decreases as the time after Ti is added. When the vacuum degassing treatment ('RH') is performed in the refining process, the addition of Ti can be performed either before or after the vacuum degassing treatment.

Slab manufacturing process

In the present invention, the molten steel composed of the chemical component system is continuously cast through a conventional refining process to make a slab. Continuous casting is preferable from the viewpoint of productivity improvement by casting at low speed and giving a weak cooling condition in the secondary cooling zone in consideration of the high possibility of occurrence of cast surface cracks in high nitrogen steel. Cooling conditions in the secondary cooling zone are important factors affecting the refinement and uniform distribution of TiN precipitates.

According to the study of the present invention, the continuous casting speed is less than 1.2 m / min, more preferably about 0.9 to 1.2 m / min. If the casting speed is less than 0.9m / min, the surface cracks are advantageous for cast surface cracking, but productivity is lower. If the casting speed is faster than 1.2m / min, the surface cracks are more likely to occur.

In the secondary cooling zone, the specific water amount is preferably as low as possible, that is, 0.3 to 0.35 l / kg. When the specific amount is less than 0.3 L / kg, it is difficult to control the proper size and number of TiN to show the effect of the present invention due to coarsening of TiN precipitates. In addition, when the specific water content exceeds 0.35L / kg, the precipitation frequency of the TiN precipitates is small, and it is difficult to control the number, size, and the like of TiN precipitates for showing the effects of the present invention.

Hot rolling process

In the present invention, it is preferable to heat the slab at 1000-1250 ° C. for 60-180 minutes. When the slab heating temperature is less than 1000 ℃, it is difficult to secure the size and number of the appropriate MnS precipitate and TiN + MnS composite precipitate for showing the effect of the present invention, when the heating temperature is more than 1250 ℃ appropriate TiN + MnS composite precipitate As the size and number of saturates and the austenite grains grow during heating, it affects the recrystallization during the rolling process, and the austenitic particles are too coarse, so that the ferrite refining effect in the post process is low, thereby deteriorating the mechanical properties of the steel. If the slab heating time is less than 60 minutes, the solidification segregation is reduced, and the time required for distributing TiN + MnS complex precipitates is insufficient. If the heating time is more than 180 minutes, the effect is saturated, resulting in the It is undesirable because not only the cost increases but also austenite grain growth in the slab affects the subsequent rolling process. If the slab is heated in the range of 1000-1100 ℃, the heating time should be 120-180 minutes.

After heating as above, it is preferable to hot-roll at a rolling ratio of 40% or more at the austenite recrystallization zone temperature. The austenite recrystallization zone temperature is affected by the emphasis and the previous reduction amount, and the austenite recrystallization zone temperature is in the range of about 1050 to 850 ° C. in consideration of the usual reduction amount in the emphasis of the present invention. In this section, a rolling ratio of at least 40% should be given. If the rolling ratio is less than 40%, the ferrite nucleation site in the austenite grain is insufficient and the effect of refining the ferrite grains due to austenite recrystallization is insufficient. It affects the precipitate behavior which effectively affects the toughness of the affected zone.

After rolling as described above, in order to prevent ferrite grain growth, it is cooled at a rate of 1 ° C./min or more up to a ferrite transformation end temperature of ± 10 ° C. Preferably, it is cooled at a rate of 1 ° C./min or more to the ferrite transformation end temperature and thereafter air-cooled. Of course, it is possible to cool the ferrite transformation temperature below the end temperature, that is, above 1 ° C / min to room temperature, but it is uneconomical. If the cooling rate is less than 1 ° C / min, it causes a grain growth of the recrystallized fine ferrite, it is difficult to secure the ferrite grain size of the steel slab less than 20㎛.

Casting of the steel in the present invention can be produced by slab by continuous casting or mold casting. In this case, if the cooling rate is fast, it is advantageous to finely disperse the precipitates, and thus, continuous casting having a high cooling rate is preferable. For the same reason, slabs are advantageously thinner. In the hot rolling process of the slab, hot charge rolling and direct rolling may be applied according to a user's use, and various known techniques such as control rolling and control cooling may be applied. In addition, heat treatment may be applied to improve the mechanical properties of the hot rolled sheet produced according to the present invention. However, even if the well-known techniques are applied to the present invention, it is natural that they are interpreted to be substantially within the technical scope of the present invention as a simple change of the present invention.

[Welding Structure]

The welded steel material provided according to the present invention is a composite structure of ferrite (70% or more) + pearlite, and the size of the ferrite grains is 20 µm or less. In addition, TiN + MnS composite precipitates have a size of 0.01-0.1 μm or more and 1.0 × 10 ⁷ or more per mm ² , and the interval is 0.5 μm or less.

When the high heat input welding is applied to such steels, the old austenite grain size is 80 μm or less. If the austenite grain size is greater than 80 µm, low-temperature structure (martensite or upper bainite) is easily formed due to the increase in hardenability, which is detrimental to the weld heat affected zone toughness. In addition, even if ferrites having different nucleation sites are produced at the old austenite grain boundaries, ferrite coalesces during grain growth, which adversely affects toughness. Therefore, the critical size of the austenite grain size of the weld heat affected zone for showing the effect of the present invention must be controlled to 80㎛ or less.

When the high heat input welding is applied and quenched as described above, the ferrite of 20 micrometers or less of the microstructure size of a heat-affected part has a phase ratio of 70% or more. If the grain size of the ferrite is larger than 20 μm, the ferrite fraction of the side plate (or allotriomorphs) that is harmful to the weld heat affected zone toughness increases. When the ferrite of the present invention has the characteristics of polygonal ferrite and acicular ferrite, it is more advantageous for toughness, which is the main function of the BN, AlN precipitates according to the present invention.

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

EXAMPLE

Steel grades having the composition as shown in Table 1 were used as a sample, dissolved in a converter, and then manufactured as slabs by a continuous casting method, and then hot rolled sheets were manufactured under the conditions of Table 3.

The test pieces for evaluating the mechanical properties of the base metal from the hot rolled plates as described above were taken at the center of the plate thickness of the rolled material, the tensile test piece was taken in the rolling direction, and the Charpy impact specimen was taken in the direction perpendicular to the rolling direction. It was.

Tensile test piece was used KS standard (KS B 0801) No. 4 test piece and the tensile test was tested at the cross head speed (5mm / mim). The impact test piece was manufactured according to KS (KS B 0809) No. 3 test piece, and the notch direction was processed on the side of the rolling direction (L-T) in the case of the base material and in the welding line direction on the welding material. In addition, in order to investigate the austenite grain size according to the maximum heating temperature of the welding heat affected zone, it is heated to 140 ℃ / sec condition for 1 second after the heating up to the maximum heating temperature (1200 ~ 1400 ℃) by using the simulation welding simulator (simulator). After holding, it was quenched with He gas. The quenched specimens were ground and corroded to determine the austenite grain size at the highest heating temperature condition by KS (KS D 0205).

The size, number, and spacing of precipitates and oxides, which have a significant effect on the microstructure analysis and the toughness of the weld affected zone after cooling, were measured by the point counting method using an image analyzer and an electron microscope. At this time, the test surface was evaluated based on 100 mm ² .

Impact toughness evaluation of the welding heat affected zone is 800-500 ℃ cooling after heating the welding conditions corresponding to about 80 kJ / cm, 150 kJ / cm, 250 kJ / cm, that is, the maximum heating temperature to 1400 ℃ After the welding heat cycles of 60 seconds, 120 seconds, and 180 seconds were applied, the surface of the test piece was polished, processed into an impact test piece, and evaluated through a Charpy impact test at -40 ° C.

Chemical composition (% by weight) C Si Mn P S Al Ti B (ppm) N (ppm) W Cu Ni Cr Mo Nb V Ca REM O (ppm) Inventive Steel 1 0.12 0.13 1.54 0.006 0.005 0.04 0.014 7 120 0.005 0.1 - - - - 0.01 - - 11 Inventive Steel 2 0.07 0.12 1.71 0.006 0.006 0.07 0.05 10 280 0.002 - 0.2 - - - 0.01 - - 12 Invention Steel 3 0.14 0.10 2.01 0.006 0.008 0.06 0.015 3 110 0.003 - - - - - 0.02 - - 10 Inventive Steel 4 0.10 0.12 1.80 0.006 0.007 0.02 0.02 5 80 0.001 0.1 - - - - 0.05 - - 9 Inventive Steel 5 0.08 0.15 2.1 0.006 0.006 0.09 0.05 15 300 0.002 - - 0.1 - - 0.05 - - 12 Inventive Steel 6 0.10 0.14 2.0 0.007 0.005 0.025 0.02 10 100 0.004 - - - 0.1 - 0.09 - - 9 Inventive Steel 7 0.13 0.14 1.6 0.007 0.007 0.04 0.015 8 115 0.15 0.1 - - - - 0.02 - - 11 Inventive Steel 8 0.11 0.15 1.52 0.007 0.006 0.06 0.018 10 120 0.001 - - - - 0.015 0.01 - - 10 Inventive Steel 9 0.13 0.21 1.42 0.007 0.005 0.025 0.02 4 90 0.002 - - 0.1 - - 0.02 0.001 - 12 Inventive Steel 10 0.07 0.16 2.2 0.008 0.010 0.045 0.025 6 100 0.05 - 0.3 - - 0.01 0.02 - 0.01 11 Inventive Steel 11 0.11 0.21 1.48 0.007 0.006 0.047 0.019 11 130 0.01 - 0.1 - - - - - - 15 Conventional Steel 1 0.05 0.13 1.31 0.002 0.006 0.0014 0.009 1.6 22 - - - - - - - - - 22 Conventional Steel 2 0.05 0.11 1.34 0.002 0.003 0.0036 0.012 0.5 48 - - - - - - - - - 32 Conventional Steel 3 0.13 0.24 1.44 0.012 0.003 0.0044 0.010 1.2 127 - 0.3 - - - 0.05 - - - 138 Conventional Steel 4 0.06 0.18 1.35 0.008 0.002 0.0027 0.013 8 32 - - - 0.14 0.15 - 0.028 - - 25 Conventional Steel 5 0.06 0.18 0.88 0.006 0.002 0.0021 0.013 5 20 - 0.75 0.58 0.24 0.14 0.015 0.037 - - 27 Conventional Steel 6 0.13 0.27 0.98 0.005 0.001 0.001 0.009 11 28 - 0.35 1.15 0.53 0.49 0.001 0.045 - - 25 Conventional Steel 7 0.13 0.24 1.44 0.004 0.002 0.02 0.008 8 79 - 0.3 - - - 0.036 - - - - Conventional Steel 8 0.07 0.14 1.52 0.004 0.002 0.002 0.007 4 57 - 0.32 0.35 - - 0.013 - - - - Conventional Steel 9 0.06 0.25 1.31 0.008 0.002 0.019 0.007 10 91 - - - 0.21 0.19 0.025 0.035 - - - Conventional Steel 10 0.09 0.26 0.86 0.009 0.003 0.046 0.008 15 142 - - 1.09 0.51 0.36 0.021 0.021 - - - Conventional Steel 11 0.14 0.44 1.35 0.012 0.012 0.030 0.049 7 89 - - - - - - 0.069 - - - Conventional steels (1, 2, 3) are invention steels (5, 32, 55) of Japanese Patent Application Laid-Open No. 9-194990, and conventional steels (4, 5, 6) are inventions of Japanese Patent Application Laid-Open No. 10-298708. Steels (14, 24, 28) and conventional steels (7, 8, 9, 10) are invention steels (48, 58, 60, 61) of JP-A-8-60292. Inventive Steel F of Patent Publication No. 11-140582

Steel grade used division Primary deoxidation sequence Dissolved oxygen after Al addition (ppm) Ti addition after finishing deoxidation (%) Casting speed (m / min) Specific quantity (ℓ / kg) Inventive Steel 1 Invention 1 Mn → Si 19 0.014 1.1 0.32 Invention 2 Mn → Si 18 0.014 1.1 0.32 Invention 3 Mn → Si 18 0.014 1.1 0.32 Comparative Material 1 Mn → Si 32 0.014 1.1 0.32 Comparative Material 2 Mn → Si 58 0.014 1.1 0.32 Inventive Steel 2 Invention 4 Mn → Si 16 0.05 1.0 0.35 Invention Steel 3 Invention 5 Mn → Si 15 0.015 1.0 0.35 Inventive Steel 4 Invention 6 Mn → Si 15 0.02 1.0 0.35 Inventive Steel 5 Invention 7 Mn → Si 12 0.05 1.2 0.30 Inventive Steel 6 Invention Material 8 Mn → Si 17 0.02 1.2 0.30 Inventive Steel 7 Invention Material 9 Mn → Si 18 0.015 1.1 0.32 Inventive Steel 8 Invention 10 Mn → Si 14 0.018 1.1 0.32 Inventive Steel 9 Invention 11 Mn → Si 19 0.02 1.1 0.32 Inventive Steel 10 Invention Material12 Mn → Si 22 0.025 1.0 0.35 Inventive Steel 11 Invention Material 13 Mn → Si 20 0.019 1.0 0.35 Conventional steel (1-11) is not specifically described manufacturing conditions

Alloy element composition ratio for showing the effect of the present invention Mn / S Ti / N N / B Al / N V / N (Ti + 2Al + 4B + V) / N Invention 1 308 1.2 17.1 3.3 0.8 8.9 Invention 2 308 1.2 17.1 3.3 0.8 8.9 Invention 3 308 1.2 17.1 3.3 0.8 8.9 Invention 4 285 1.8 28.0 2.5 0.4 7.3 Invention 5 251 1.4 36.7 5.5 1.8 14.2 Invention 6 257 2.5 16.0 2.5 6.3 14.0 Invention 7 350 1.7 20.0 3.0 1.7 9.5 Invention Material 8 400 2.0 10.0 2.5 9.0 16.4 Invention Material 9 229 1.3 14.4 3.5 1.7 10.3 Invention 10 253 1.5 12.0 5.0 0.8 12.7 Invention 11 284 2.2 22.5 2.8 2.2 10.2 Invention Material12 220 2.5 16.7 4.5 2.0 13.7 Invention Material 13 247 1.5 11.8 3.6 - 9.0 Conventional Steel 1 218 4.1 13.8 0.6 - 5.7 Conventional Steel 2 447 2.5 96.0 0.8 - 4.0 Conventional Steel 3 480 0.8 105.8 0.4 - 1.5 Conventional Steel 4 657 4.1 4.0 0.8 8.8 15.5 Conventional Steel 5 440 6.5 4.0 1.1 18.5 28.1 Conventional Steel 6 980 3.2 2.6 0.4 16.1 21.6 Conventional Steel 7 720 1.0 9.9 2.5 - 6.5 Conventional Steel 8 760 1.2 14.3 0.4 - 2.2 Conventional Steel 9 655 0.8 9.1 2.1 3.9 9.2 Conventional Steel 10 287 0.6 9.5 3.2 1.5 8.9 Conventional Steel 11 113 5.5 12.7 3.4 7.8 20.3

Steel grade used division Heating temperature (℃) Heating time (min) Rolling Start Temperature (℃) Rolling end temperature (℃) Rolling amount / accumulated loading amount at recrystallization area (%) Cooling rate (℃ / min) Invention 2 Inventive Example 1 1150 170 1030 850 65/80 5 Inventive Example 2 1200 130 1040 850 65/80 5 Inventive Example 3 1240 90 1040 850 65/80 5 Comparative Example 1 1050 60 1040 850 65/80 5 Comparative Example 2 1300 250 1035 850 65/80 5 Invention 1 Inventive Example 4 1200 130 1020 840 65/80 6 Invention 3 Inventive Example 5 1200 130 1040 850 65/80 6 Comparative Material 1 Comparative Example 3 1210 120 1030 860 65/80 0.01 Comparative Material 2 Comparative Example 4 1210 120 1030 860 65/80 35 Invention 4 Inventive Example 6 1180 150 1020 860 60/80 5 Invention 5 Inventive Example 7 1190 140 1010 850 60/80 5 Invention 6 Inventive Example 8 1220 110 1010 840 60/75 6 Invention 7 Inventive Example 9 1220 110 1020 840 60/75 7 Invention Material 8 Inventive Example 10 1210 120 1010 850 60/75 7 Invention Material 9 Inventive Example 11 1220 110 1000 840 55/70 5 Invention 10 Inventive Example 12 1210 120 1010 830 55/70 6 Invention 11 Inventive Example 13 1230 100 1000 850 55/70 5 Invention Material12 Inventive Example 14 1220 110 1020 840 55/70 5 Invention Material 13 Inventive Example 15 1210 130 1020 840 65/75 5 Conventional Steel 11 1200 - Ar ₃ or higher 960 80 Cooling Cooling controls the cooling rate to 500 ℃, the temperature after the ferrite transformation is completed, and thereafter, the manufacturing conditions of air-cooled conventional steel (1-10) are not specified.

division TiN + MnS precipitate characteristics Base material texture and mechanical properties Count (pcs / mm ² ) Average size (㎛) Average interval (㎛) Thickness (mm) Yield strength (MPa) Tensile Strength (MPa) Elongation (%) FGS (μm) Ferrite Percentage (%) Impact toughness at -40 ° C (J) Inventive Example 1 2.4 X ^{10 8} 0.016 0.25 25 394 553 38 11 82 358 Inventive Example 2 3.2 X ^{10 8} 0.017 0.24 25 395 551 39 9 83 362 Inventive Example 3 2.5 X ^{10 8} 0.012 0.26 25 396 550 39 10 83 357 Comparative Example 1 2.3 X 10 ⁶ 0.174 1.6 25 393 554 26 16 70 206 Comparative Example 2 3.4 X 10 ⁶ 0.165 1.8 25 792 860 17 17 21 45 Inventive Example 4 3.2 X ^{10 8} 0.025 0.32 30 396 558 38 11 83 349 Inventive Example 5 2.6 X ^{10 8} 0.013 0.34 30 396 562 38 10 83 354 Comparative Example 3 1.3 X 10 ⁶ 0.182 1.2 30 384 564 30 18 73 220 Comparative Example 4 4.3X10 ⁶ 0.177 1.4 30 392 582 29 17 74 208 Inventive Example 6 3.3 X ^{10 8} 0.026 0.35 30 390 563 38 10 82 364 Inventive Example 7 4.6 X ^{10 8} 0.024 0.32 35 390 564 39 10 85 360 Inventive Example 8 4.3X10 ⁸ 0.014 0.40 35 392 542 36 11 82 365 Inventive Example 9 5.6 X ^{10 8} 0.028 0.29 35 391 536 37 10 84 359 Inventive Example 10 5.2 X ^{10 8} 0.021 0.28 35 394 566 36 10 83 375 Inventive Example 11 3.7 X ^{10 8} 0.029 0.25 40 390 566 37 12 83 364 Inventive Example 12 3.2 X ^{10 8} 0.025 0.31 40 396 542 38 11 85 356 Inventive Example 13 3.3 X ^{10 8} 0.042 0.34 40 406 564 38 12 82 348 Inventive Example 14 3.6X10 ⁸ 0032 0.28 40 387 550 37 10 83 349 Inventive Example 15 4.2 X ^{10 8} 0.018 0.26 30 389 549 39 9 86 368 Conventional Steel 1 35 406 436 Conventional Steel 2 35 405 441 Conventional Steel 3 25 629 681 Conventional Steel 4 Precipitates of MgO-TiN 3.03 × 10 ⁶ pcs / mm ² 40 472 609 Conventional Steel 5 Precipitates of MgO-TiN 4.07 × 10 ⁶ pcs / mm ² 40 494 622 Conventional Steel 6 Precipitates of MgO-TiN 2.80 × 10 ⁶ pcs / mm ² 50 812 912 Conventional Steel 7 25 629 681 Conventional Steel 8 50 504 601 Conventional Steel 9 60 526 648 Conventional Steel 10 60 760 829 Conventional Steel 11 50 401 514

As shown in Table 5, the number of precipitates (Ti + MnS composite precipitates) of the hot rolled material produced by the present invention has a range of 1.0 × ^{10 8} / mm ² or more, whereas the precipitates of conventional materials are 4.07X10 ⁵ It showed a range of less than / mm ² . It can be seen that while the invention material has a very fine precipitate size, the number thereof is also significantly increased. In addition, in the matrix structure of the present invention, the steel of the present invention is not only fine in the particle size of about 8㎛, but also consists of a high fraction of ferrite phase of 87% or more.

division Austenitic grain size of welding heat affected zone (㎛) Microstructure of welding heat affected zone with 100kJ / cm input heat Mechanical Properties of Weldment Reproduction Weld Heat Affected Zone -40 ℃ Impact Toughness (J) (Maximum Heating Temperature: 1400 ℃) 1200 (℃) 1300 (℃) 1400 (℃) Ferrite Percentage (%) Ferrite Average Grain Size (㎛) Δt _800-500 = 180 seconds Δt _800-500 = 120 seconds Δt _800-500 = 180 seconds Yield strength (kg / ㎡) Tensile Strength (kg / ㎡) Impact Toughness (J) Transition temperature (℃) Impact Toughness (J) Transition temperature (℃) Inventive Example 1 23 33 56 73 16 370 -74 330 -67 294 -62 Inventive Example 2 22 34 55 76 15 383 -76 353 -69 301 -63 Inventive Example 3 23 32 56 74 17 365 -72 331 -67 298 -63 Comparative Example 1 54 84 182 36 32 126 -43 47 -34 26 -27 Comparative Example 2 65 91 198 37 35 104 -40 35 -32 18 -26 Inventive Example 4 25 37 65 75 18 353 -71 325 -68 287 -64 Inventive Example 5 26 40 57 74 16 362 -71 333 -67 296 -61 Comparative Example 3 48 78 220 58 22 182 -44 87 -36 36 -28 Comparative Example 4 56 82 254 52 26 176 -44 79 -35 32 -29 Inventive Example 6 25 31 53 76 17 386 -73 353 -69 305 -62 Inventive Example 7 24 34 55 74 18 367 -71 338 -67 293 -63 Inventive Example 8 27 36 53 73 14 364 -71 334 -67 294 -61 Inventive Example 9 24 36 52 74 17 367 -72 335 -67 285 -62 Inventive Example 10 22 35 53 73 18 385 -72 345 -66 294 -61 Inventive Example 11 26 34 64 74 16 358 -71 324 -68 285 -63 Inventive Example 12 27 38 64 74 18 355 -71 324 -67 284 -62 Inventive Example 13 24 32 54 75 16 367 -72 336 -68 285 -63 Inventive Example 14 25 31 58 72 17 365 -72 330 -68 280 -63 Inventive Example 15 24 32 54 76 14 368 -72 345 -68 286 -63 Conventional Steel 1 187 -51 Conventional Steel 2 156 -48 Conventional Steel 3 148 -50 Conventional Steel 4 230 93 143 -48 132 (0 ℃) Conventional Steel 5 180 87 132 -45 129 (0 ℃) Conventional Steel 6 250 47 153 -43 60 (0 degrees Celsius) Conventional Steel 7 141 -54 -61 Conventional Steel 8 156 -59 -48 Conventional Steel 9 145 -54 -42 Conventional Steel 10 138 -57 -45 Conventional Steel 11 141 -43 219 (0 ℃)

As shown in Table 6, the austenitic grain size at the maximum heating temperature of 1400 ° C., such as the weld heat affected zone, ranges from 52 to 65 μm in the case of the present invention, while the conventional material has a very high roughness of about 180 μm or more. Therefore, it can be seen that the steel of the present invention has a very good effect of suppressing austenite grains in the weld heat affected zone during welding. In addition, the ferrite phase fraction of the steel of the present invention was composed of about 70% or more at a welding heat input amount of 100 kJ / cm.

On the other hand, when comparing the impact toughness of the weld heat affected zone during high heat input welding, -40 ° C. welding in the case of the present invention under high heat input welding heat input condition in which the welding heat input amount is 250 kJ / cm (the cooling time of 800-500 ° C is 180 seconds). The impact toughness of the heat affected zone shows an excellent toughness value of about 280 J or more, and the transition temperature indicates a value of about -60 ° C. or less, indicating that the impact resistance of the high heat input welding heat affected zone is excellent. On the other hand, in the same high heat input heat input condition, conventional steel shows impact toughness value of about 200J at 0 ° C heat affected zone, and transition temperature is about -60 ° C.

As described above, the present invention has a useful effect of using a TiN + MnS composite precipitate to provide a structural structural steel for welding in which the toughness and strength of the weld heat affected zone are simultaneously improved.

Claims (11)

By weight C: 0.03-0.17%, Si: 0.01-0.5%, Mn: 1.0-2.5%, Ti: 0.005-0.2%, Al: 0.0005-0.1%, N: 0.008-0.030%, B: 0.0003-0.01 %, W: 0.001-0.2%, P: 0.03% or less, S: 0.003-0.05%, O: 0.005% or less, 1.2≤Ti / N≤2.5, 10≤N / B≤40, 2.5≤Al / N≤ 7, 6.5 ≤ (Ti + 2 Al + 4B) / N ≤ 14, 220 ≤ Mn / S ≤ 400, is composed of the remaining Fe and other impurities, the microstructure of the ferrite and perlite composite structure of less than 20㎛ Steel for welded structures having a composite precipitate of TiN + MnS. The steel material according to claim 1, wherein V is contained in an amount of 0.01 to 0.2%, a ratio of V and N (V / N) is 0.3 to 9, and 7≤ (Ti + 2Al + 4B + V) / N≤17. Welded structural steels having a composite precipitate of TiN + MnS, characterized in that it satisfies. According to claim 1 or 2, wherein the steel is Ni: 0.1 to 3.0%, Cu: 0.1-1.5%, Nb: 0.01 to 0.1%, Mo: 0.05 to 1.0%, Cr: 0.05 to 1.0% A welded structural steel having a composite precipitate of TiN + MnS, characterized by containing one or two or more selected and one or two selected from the group of Ca: 0.0005-0.005% and REM: 0.005 to 0.05%. The composite precipitate of TiN + MnS according to claim 1 or 2, wherein the composite precipitate of TiN + MnS having a thickness of 0.01-0.1 μm is distributed at 1.0 × 10 ⁷ / mm 2 or more at intervals of 0.5 μm or less. Steel for welding structure having By weight C: 0.03-0.17%, Si: 0.01-0.5%, Mn: 1.0-2.5%, Ti: 0.005-0.2%, Al: 0.0005-0.1%, N: 0.008-0.030%, B: 0.0003-0.01 %, W: 0.001-0.2%, P: 0.03% or less, S: 0.003-0.05%, O: 0.005% or less, 1.2≤Ti / N≤2.5, 10≤N / B≤40, 2.5≤Al / N≤ The steel slab which satisfies 7, 6.5≤ (Ti + 2Al + 4B) / N≤14, 220≤Mn / S≤400 and is composed of the remaining Fe and other impurities is heated in the range of 1000-1250 ° C for 60-180 minutes. Later, in the austenite recrystallization zone, hot-rolled at a rolling ratio of 40% or more, followed by cooling at a rate of 1 ° C./min or more at a ferrite transformation end temperature of ± 10 ° C., to manufacture a welded structural steel having a TiN + MnS composite precipitate. Way. 6. The steel material according to claim 5, wherein V is contained in an amount of 0.01 to 0.2%, a ratio of V and N (V / N) is 0.3 to 9, and 7≤ (Ti + 2Al + 4B + V) / N≤17. Method for producing a welded structural steel having a composite precipitate of TiN + MnS characterized in that it satisfies. The steel material according to claim 5 or 6, wherein the steel comprises Ni: 0.1 to 3.0%, Cu: 0.1 to 1.5%, Nb: 0.01 to 0.1%, Mo: 0.05 to 1.0%, and Cr: 0.05 to 1.0%. 1 or 2 or more selected, and Ca: 0.0005-0.005%, REM: 0.005 to 0.05% of the welded structural steel having a composite precipitate of TiN + MnS characterized in that it contains one or two selected from the group Way. According to claim 5, The slab is added to the molten steel deoxidation element having a greater deoxidizing power than Ti before the Ti input, deoxidized dissolved oxygen of the molten steel to 30ppm or less, and added within 10 minutes so that the content of Ti is 0.005-0.02% Method for producing a welded structural steel having a composite precipitate of TiN + MnS, characterized in that made by continuous casting. 9. The slab according to claim 5 or 8, wherein the slab is continuously cast by casting the molten steel at a rate of 0.9 to 1.2 m / min and weakly cooling it to a specific amount of 0.3 to 0.35 l / kg in a secondary cooling zone. Method for producing a welded structural steel having a composite precipitate of TiN + MnS. The heat input welding is applied to the steel material (base material) of claim 4, thereby producing a prior austenite of 80 µm or less in the weld heat affected zone, and then quenching the ferrite having a microstructure of 20 µm or less in the weld heat affected zone. Welded structure with excellent toughness of weld heat affected zone with over 70% phase fraction. The weld structure of claim 10, wherein the ferrite is polygonal ferrite and acicular ferrite.