JP3362371B2 - Steam turbine and steam turbine power plant - Google Patents

Description

Detailed Description of the Invention

[0001]

BACKGROUND OF THE INVENTION 1. Field of the Invention The present invention relates to a novel high-efficiency high-temperature steam turbine, and more particularly to a steam turbine having a main steam temperature and / or a reheat steam temperature of 610 to 660 ° C. and a steam turbine power generation using the steam turbine. Regarding the plant.

[0002]

2. Description of the Related Art A conventional steam turbine has a maximum steam temperature of 56.
The temperature was 6 ° C and the vapor pressure was 246 atg. However, from the viewpoint of depletion of fossil fuels such as oil and coal, energy saving, and prevention of environmental pollution, there is a demand for higher efficiency of thermal power plants.
Increasing the steam temperature of the steam turbine is the most effective means to increase power generation efficiency. These high-efficiency turbine materials include 1Cr-1Mo-1 / 4V as a rotor material.
Ferrite low alloy forged steel, 11Cr-1Mo-VN
bN forged steel, 1Cr-1Mo-1 / as casing material
4V ferritic low alloy cast steel and 11Cr-1Mo-V
-Nb-N cast steel is known, and particularly, as these materials having higher high temperature strength, austenitic alloys disclosed in JP-A-62-180044 and JP-A-61-23749, The martensitic steels disclosed in JP-A-4-147948, JP-A-2-290950 and JP-A-4-371551 are known.

[0003]

Although the above publication discloses a rotor material, a casing material and the like, as described above, the steam turbine and the thermal power plant system associated with higher temperatures are not considered at all.

Further, an ultrahigh temperature and high pressure steam turbine is known from Japanese Patent Laid-Open No. 62-248806, but no consideration is given to the entire plant system.

An object of the present invention is to make steam temperatures 610 to 660.
(EN) It is possible to provide a steam turbine having a high heat efficiency that enables a high temperature of ℃ by a ferritic heat-resistant steel and a steam turbine power plant using the same.

[0006]

The present invention relates to a steam turbine power plant having a low-pressure turbine in which a high-pressure turbine and an intermediate-pressure turbine are connected and two units are connected in tandem, wherein the high-pressure turbine and the intermediate-pressure turbine are The steam inlet temperature to the first stage moving blade is 610 to 660 ° C (preferably 61 ° C).
5 to 640 ° C., preferably 620 to 630 ° C.), the low pressure turbine has a steam inlet temperature to the first stage moving blades of 380 to 475 ° C. (preferably 400 to 430 ° C.). and all stages of the moving blades Ru exposed to the steam inlet temperature of the intermediate-pressure turbine, all the stages and the inner casing of the vane is made from a high strength martensite steel containing Cr8~13 wt%, the high-pressure turbine and the medium
The rotor shaft of the pressure turbine is by weight, C0.05-0.5.
20%, Si 0.15% or less, Mn 0.05-1.5%,
Cr 9.5 to 13%, Ni 0.05 to 1.0%, V0.0
5 to 0.35%, Nb 0.01 to 0.20%, N 0.01 to
0.06%, Mo 0.05-0.5%, W 1.0-4.0
%, Co2 to 10%, B 0.0005 to 0.03%
High strength martensitic steel containing at least 78% Fe
It consists of a steam turbine power plant.

Further, the present invention comprises a rotor shaft, a rotor blade embedded in the rotor shaft, a stator vane for guiding the inflow of water vapor into the rotor blade, and an inner casing for holding the stator vane. The temperature of the steam flowing into the first stage of the moving blade is 610 to 660 ° C. and the pressure is 250 kg / cm ² or more (preferably 246 to 316 kg / cm ² ) or 170 to 200 kg.
/ Cm ² of the steam turbine, wherein the rotor shaft and at least the first stage of the moving blades and the stationary blades have respective steam temperatures (preferably 610 ° C, 625 ° C, 640 ° C, 650 ° C, 66 ° C).
9.5 to 13% by weight of Cr (preferably 10.5 to 11.5%) having a 10 ⁵ hour creep rupture strength of 15 kg / mm ² or more (preferably 17 kg / mm ² or more) at a temperature corresponding to 0 ° C).
5% by weight), which is made of high-strength martensitic steel having a fully tempered martensite structure, and the inner casing has a 10 ⁵ hour creep rupture strength of 10 kg / mm ² or more (preferably at a temperature corresponding to each steam temperature). Is 10.
The steam turbine is characterized by comprising a martensitic cast steel containing 8 to 9.5 wt% of Cr (5 kg / mm ² or more).

Further, according to the present invention, a steam having a rotor shaft, a rotor blade planted in the rotor shaft, a stator vane for guiding the inflow of water vapor into the rotor blade, and an inner casing for holding the stator vane. In the turbine, at least the first stage of the rotor shaft, the moving blades and the stationary blades is the weight, and C
0.05 to 0.20%, Si 0.15% or less, Mn 0.05
~ 1.5%, Cr 9.5-13%, Ni 0.05-1.0
%, V0.05 to 0.35%, Nb0.01 to 0.20%,
N0.01-0.06%, Mo0.05-0.5%, W1.
0-4.0%, Co2-10%, B0.0005-0.0
It consists of a high-strength martensitic steel containing 3% and having at least 78% Fe, the inner casing having a C0.
06-0.16%, Si 0.5% or less, Mn 1% or less,
Ni 0.2-1.0%, Cr 8-12%, V 0.05-0.0.
35%, Nb 0.01 to 0.15%, N 0.01 to 0.8
%, Mo1% or less, W1-4%, B0.0005-0.0
A steam turbine comprising a high-strength martensitic steel containing 03% and having 85% or more Fe.

Further, according to the present invention, a high pressure having a rotor shaft, a rotor blade planted in the rotor shaft, a stator vane guiding the inflow of water vapor into the rotor blade, and an inner casing holding the stator vane. In the steam turbine, the moving blade is 1
The rotor shaft has 0 or more stages, the first stage is a double flow, and the rotor shaft has a bearing center distance (L) of 5000 mm or more (preferably 5200 to 5500 mm) and a minimum diameter (D) in a portion where the vanes are provided. 600mm or more (preferably 620)
To 700 mm) and the (L / D) is 8.0 to 9.0 (preferably 8.3 to 8.7), and is made of high strength martensitic steel containing 9 to 13% by weight of Cr. preferable.

Further, the present invention has a rotor shaft, a rotor blade planted in the rotor shaft, a stator vane for guiding the inflow of water vapor into the rotor blade, and an inner casing for holding the stator vane. In the pressure steam turbine, the rotor blades have a symmetrical structure having six or more stages each, and the rotor shaft has a double-flow structure in which the first stage is implanted. The rotor shaft has a bearing center distance (L) of 5200 mm. Above (preferably 5300 to 5800 mm) and the minimum diameter (D) at the portion where the vanes are provided is above 620 mm (preferably 62)
0 to 680 mm) and the (L / D) is 8.2 to 9.2.
9 to 13% by weight of Cr (preferably 8.5 to 9.0)
It is preferably made of a high-strength martensitic steel containing.

Further, according to the present invention, there is provided a low-pressure rotor having a rotor shaft, a rotor blade embedded in the rotor shaft, a stator vane for guiding the inflow of water vapor into the rotor blade, and an inner casing for holding the stator vane. In the steam turbine, the rotor blades are symmetrically provided with eight or more stages each, and the rotor shaft has a double-flow structure in which the first stage is implanted in the center portion of the rotor shaft. The rotor shaft has a bearing center distance (L) of 7200 mm or more ( 7400 to 7600 mm) and the minimum diameter (D) at the portion where the vanes are provided is 1150 mm or more (preferably 12).
0 to 1350 mm) and the (L / D) is 5.4 to
Ni 3.25 which is 6.3 (preferably 5.7 to 6.1)
It is preferably made of a Ni-Cr-Mo-V low alloy steel containing 4.25% by weight, and the final stage rotor blade is preferably made of a Ti-based alloy having a blade length of 40 inches or more.

Further, according to the present invention, in a steam turbine power plant including a low-pressure turbine in which a high-pressure turbine and an intermediate-pressure turbine are connected and two units are connected in tandem, the high-pressure turbine and the intermediate-pressure turbine are connected to the first-stage rotor blades. Has a steam inlet temperature of 610 to 660 ° C., the low pressure turbine has a steam inlet temperature to the first stage moving blade of 380 to 475 ° C., the first stage moving blade planting portion of the rotor shaft of the high pressure turbine and the metal of the first stage moving blade. The temperature should not fall below 40 ° C (preferably 20 to 35 ° C lower than the steam temperature) below the steam inlet temperature to the first-stage moving blade of the high-pressure turbine, and the first-stage moving blade of the rotor shaft of the intermediate-pressure turbine should be planted. Part and the metal temperature of the first-stage rotor blade are 75 ° C. or higher than the steam inlet temperature to the first-stage rotor blade of the intermediate-pressure turbine (preferably 50 to 50 0 ℃ lower) as not rotate under the high-pressure turbine and even without least the intermediate pressure turbine Ri Do martensitic steel stage moving blade contains Cr9.5~13 wt%, the high-pressure turbine and the intermediate pressure turbine of
Rotor shaft weight is C0.05-0.20%, Si
0.15% or less, Mn 0.05-1.5%, Cr 9.5-
13%, Ni 0.05-1.0%, V0.05-0.35
%, Nb 0.01 to 0.20%, N 0.01 to 0.06%,
Mo 0.05-0.5%, W 1.0-4.0%, Co2-
10%, including B 0.0005 to 0.03%, 78% or more
In the steam turbine power plant according to claim Rukoto made of a high strength martensite steel having the Fe.

Furthermore, the present invention provides a coal-fired boiler, a steam turbine driven by the steam obtained by the boiler, and a single machine or two driven by the steam turbine.
In a coal-fired thermal power plant including a generator having a power generation output of 1000 MW or more, preferably 2 units, the steam turbine includes a high-pressure turbine, an intermediate-pressure turbine connected to the high-pressure turbine, and two low-pressure turbines. A high-pressure turbine and a medium-pressure turbine have a steam inlet temperature of 610 to 660 ° C. to the first-stage moving blade, and the low-pressure turbine has a steam inlet temperature of 380 to 475 to the first-stage moving blade.
C. and steam heated by the superheater of the boiler to a temperature higher than the steam inlet temperature to the first-stage moving blades of the high-pressure turbine by 3 ° C. or more (preferably 3-10 ° C., more preferably 3-7 ° C.). The steam that has flowed into the first-stage moving blade of the high-pressure turbine and has exited from the high-pressure turbine is heated by the reheater of the boiler at a temperature of 2 ° C. or more (preferably 2-10 ° C.) from the steam inlet temperature to the first-stage moving blade of the intermediate-pressure turbine. (More preferably 2 to 5 ° C.) It is heated to a high temperature and flows into the first-stage moving blade of the intermediate-pressure turbine, and the steam discharged from the medium-pressure turbine is fed to the first-stage moving blade of the low-pressure turbine by the economizer of the boiler. 3 ° C or more (preferably 3 to 1) from the steam inlet temperature of
0 ° C., with more preferably to flow into the first stage rotor blades 3 to 6 ° C.) the heated high temperature low-pressure turbine, the high
The rotor shafts of the pressure turbine and medium-pressure turbine are heavy
And C0.05 to 0.20%, Si 0.15% or less, Mn
0.05-1.5%, Cr 9.5-13%, Ni 0.05-
1.0%, V0.05-0.35%, Nb0.01-0.2
0%, N 0.01 to 0.06%, Mo 0.05 to 0.5%
, W1.0-4.0%, Co2-10%, B0.0005
High strength, containing ~ 0.03% and having Fe of 78% or more
It is a coal-fired thermal power plant characterized by being made of martensitic steel .

Furthermore, according to the present invention, in the above-mentioned low-pressure steam turbine, the steam inlet temperature to the first stage moving blade is 380.
˜475 ° C. (preferably 400˜450 ° C.), and the rotor shaft has C0.2-0.3% by weight and Si.
0.05% or less, Mn 0.1% or less, Ni 3.25 to 4.2
5%, Cr 1.25 to 2.25%, Mo 0.07 to 0.20
%, V0.07 to 0.2%, and Fe 92.5% or more, preferably made of a low alloy steel.

According to the present invention, in the above-mentioned high-pressure steam turbine, the moving blade has 7 or more stages (preferably 9 to 12 stages) and the blade length is 35 to 2 from the upstream side to the downstream side of the steam flow.
The rotor shaft has a diameter of 10 mm, and the diameter of the moving blade is larger than the diameter of the portion corresponding to the stationary blade. The axial width of the moving portion is three stages or more (preferably, the downstream side is larger than the upstream side). 4 to 7 steps), and the ratio to the blade length is 0.6 to 1.0 (preferably 0.6).
5 to 0.95), it is preferable that it becomes smaller from the upstream side to the downstream side.

Further, in the above-mentioned high-pressure steam turbine,
In the present invention, the moving blade has 7 stages or more and the blade length is 35 to 210 mm from the upstream side to the downstream side of the steam flow, and the ratio of the blade lengths of adjacent stages is 1.2 or less (preferably 1.
10 to 1.15), the ratio gradually increases on the downstream side,
It is preferable that the length of the blade is larger on the downstream side than on the upstream side.

Further, in the above-mentioned high-pressure steam turbine,
According to the present invention, the rotor blade has seven stages or more and the blade portion length is 35 to 210 mm from the upstream side to the downstream side of the steam flow, and the axial width of the portion of the rotor shaft corresponding to the stationary blade portion is the above-mentioned. The downstream side has two or more stages (preferably 2
(4 steps) Gradually small, and the ratio of the moving blade to the downstream blade length is 0.65 to 1.8 (preferably 0.7 to 1.).
In the range of 7), it is preferable that the ratio gradually decreases toward the downstream side.

According to the present invention, in the above-mentioned medium-pressure steam turbine, the moving blades are symmetrically arranged in six stages or more (preferably 6 to 9).
Step) having a double-flow structure and a blade length of 100 to 300 mm from the upstream side to the downstream side of the water vapor flow, and the diameter of the rotor blade embedded portion of the rotor blade is larger than the diameter of the portion corresponding to the stationary blade, The axial width of the implant portion is gradually increased in the downstream side in two steps or more (preferably 3 to 6 steps) as compared with the upstream side, and the ratio to the blade length is 0.45 to 0.75. (Preferably 0.5-0.7)
It is preferable that the diameter becomes smaller from the upstream side to the downstream side.

Further, in the above-mentioned medium-pressure steam turbine according to the present invention, the moving blade has a double-flow structure having six or more stages symmetrically and the blade length is 10 from the upstream side to the downstream side of the steam flow.
The length of the adjacent blades is 0 to 300 mm, and the length of the adjacent blades is larger on the downstream side than on the upstream side, and the ratio is 1.3 or less (preferably 1.1 to 1.2) gradually on the downstream side. It is preferable that it is large.

Further, in the above-mentioned medium-pressure steam turbine according to the present invention, the moving blade has a double-flow structure having symmetrically six stages or more, and the blade length is 10 from the upstream side to the downstream side of the steam flow.
0 to 300 mm, and the axial width of the portion of the rotor shaft corresponding to the stationary vane portion is 2 on the downstream side compared to the upstream side.
The number of stages is gradually reduced by more than one stage (preferably 3 to 6 stages), and the ratio of the moving blade to the downstream blade length is 0.45 to 1.60 (preferably 0.5 to 1.5). It is preferable that the ratio is gradually reduced toward the downstream side.

In the low-pressure steam turbine according to the present invention, the moving blades are symmetrically arranged in eight stages or more (preferably 8 to 8 stages).
(10 stages) having a double-flow structure and a blade length of 90 to 1300 mm from the upstream side to the downstream side of the steam flow, and the diameter of the rotor blade on which the rotor blade is implanted is larger than the diameter of the portion corresponding to the stationary blade. The axial width of the implanted portion is gradually increased in the downstream side by 3 steps or more (preferably 4 to 7 steps) as compared with the upstream side, and the ratio to the blade length is 0.15 to 1. 0 (preferably 0.1)
5 to 0.91), it is preferably smaller from the upstream side to the downstream side.

Further, the present invention is the above-described low-pressure steam turbine, wherein the moving blade has a double-flow structure having symmetrically eight stages or more and the blade portion length is 90 to 1300 mm from the upstream side to the downstream side of the steam flow, The blade length of each adjacent stage is larger on the downstream side than on the upstream side, and the ratio is gradually within the range of 1.2 to 1.7 (preferably 1.3 to 1.6). It is preferable that the ratio is large on the downstream side.

Further, in the low-pressure steam turbine according to the present invention, the moving blade has a double flow structure having symmetrically eight stages or more and the blade length is 90 to 1300 mm from the upstream side to the downstream side of the steam flow, The axial width of the portion of the rotor shaft corresponding to the stationary blade portion is gradually increased in the downstream side by 3 or more steps (preferably 4 to 7 steps) as compared with the upstream side, and is adjacent to the moving blade. The ratio to the matching downstream blade length is 0.2 to 1.4 (preferably 0.25 to 1.
In the range of 25), it is preferable that the ratio gradually decreases toward the downstream side.

The present invention is a high-pressure steam turbine having a rotor shaft, a rotor blade planted on the rotor shaft, a stator vane guiding the inflow of water vapor into the rotor blade, and an inner casing holding the stator vane. In, the moving blade has seven or more stages, and the rotor shaft has a diameter of a portion corresponding to the stationary blade smaller than a diameter of a portion corresponding to the moving blade implanting portion,
The axial width of the diameter corresponding to the stationary blade is gradually increased in two or more stages (preferably 2 to 4 stages) on the upstream side of the steam flow as compared to the downstream side. The width between the last stage and the front stage is 0.75 to 0.95 times (preferably 0.8) times the width between the second stage and the third stage of the moving blade.
.About.0.9 times, more preferably 0.84 to 0.88), and the width of the rotor shaft in the axial direction of the moving blade portion is not less than three stages (preferably at the downstream side of the steam flow compared to the upstream side). Is 4 to 7 steps), and the axial width of the final stage of the moving blade is 1 to 2 times (preferably 1.4 to 4) the axial width of the second stage. It is preferably 1.7 times).

According to the present invention, a medium pressure steam having a rotor shaft, a rotor blade planted on the rotor shaft, a stator vane for guiding the inflow of water vapor into the rotor blade, and an inner casing for holding the stator vane. In the turbine, the moving blade has six stages or more, and the rotor shaft has a diameter of a portion corresponding to the stationary blade smaller than a diameter of a portion corresponding to the moving blade implanting portion,
The axial width of the diameter corresponding to the stationary blade is gradually increased in two stages or more (preferably 3 to 6 stages) on the upstream side of the steam flow as compared to the downstream side. The width between the last stage and the front stage is 0.55-0.8 times (preferably 0.6-0.0) times the width between the first stage and the second stage of the moving blade.
7 times), and the width of the rotor shaft in the axial direction of the moving blade portion implantation portion is gradually increased in two or more stages (preferably 3 to 6 stages) in the downstream side of the steam flow compared to the upstream side. The axial width of the final stage of the moving blade is 0.8 to 2 times (preferably 1 to 2) the axial width of the first stage.
It is preferably 1.5 times).

The present invention is a low-pressure steam turbine having a rotor shaft, a rotor blade planted in the rotor shaft, a stator vane for guiding the inflow of water vapor into the rotor blade, and an internal casing for holding the stator vane. In the above, the moving blade has a double-flow structure having eight or more steps symmetrically, and the rotor shaft has a diameter of a portion corresponding to the stationary blade smaller than a diameter of a portion corresponding to the moving blade implanting portion. The axial width of the diameter corresponding to the blade is gradually increased on the upstream side of the steam flow in three steps or more (preferably 4 to 7 steps) as compared with the downstream side, and the final stage of the moving blade. The width between the front and the front of the rotor blade is 1.5 to 2.5 times (preferably 1.7 to 2.2 times) the width between the first stage and the second stage of the rotor blade. The axial width of the moving blade part of the moving part is smaller in the downstream side of the steam flow than in the upstream side. 3 or more steps (preferably 4 to 7)
The axial width of the final stage of the moving blade is 2 to 3 times (preferably 2.2 to 2.7 times) the axial width of the first stage. Preferably there is.

The structure of the high pressure, medium pressure and low pressure turbines described above can be the same structure for any of the steam temperatures used of 610 to 660 ° C.

In the rotor material of the present invention, in order to obtain high temperature strength, low temperature toughness, and high fatigue strength as a fully tempered martensite structure, the Cr equivalent calculated by the following equation should be adjusted to 4 to 8 components. Is preferred.

In the casing material made of the heat-resistant cast steel of the present invention, tempered martensite (δ
It is preferable to adjust the Cr equivalent calculated by the following equation to 4 to 10 in order to adjust the alloy composition so as to have a structure of ferrite 5% or less) and obtain high temperature temperture, low temperature toughness and high fatigue strength. .

Cr equivalent = Cr + 6Si + 4Mo + 1.5
W + 11V + 5Nb-40C-30N-30B-2Mn
-4Ni-2Co In the 12Cr heat-resistant steel of the present invention, especially when used in steam at 621 ° C or higher, 625 ° C, 10 ⁵ h creep rupture strength 10 kgf / mm ² or higher, room temperature impact absorption energy 1 kgf-m. The above is preferable.

(1) The reasons for limiting the composition of the ferritic heat-resisting steel constituting the high pressure and medium pressure rotors, blades, nozzles, inner casing fastening bolts and intermediate pressure part first stage diaphragm of the steam turbine in the present invention will be explained.

C is an essential element for ensuring hardenability, precipitating carbides in the tempering heat treatment process to enhance high temperature strength, and 0.05% or more is necessary for obtaining high tensile strength. It is an element, but if it exceeds 0.20%, the metal structure becomes unstable when exposed to high temperature for a long time, and the long-term creep rupture strength decreases, so it is 0.05-0.20%.
Limited to Desirably 0.08 to 0.13%,
In particular, 0.09 to 0.12% is preferable.

Mn is added as a deoxidizing agent and the like, and its effect is achieved by adding a small amount, and addition of a large amount exceeding 1.5% lowers the creep rupture strength, which is not preferable. Especially 0.03 to 0.20% or 0.3 to 0.7%
Is preferable, and more preferably 0.35 to 0.65%. Higher strength can be obtained with less Mn. Further, the larger the amount of Mn, the better the workability.

Although Si is also added as a deoxidizing agent, Si deoxidizing is not required according to the steelmaking technology such as vacuum C deoxidizing method. By lowering Si, it is possible to prevent harmful δ-ferrite structure from being generated and to prevent deterioration of toughness due to segregation of grain boundaries. Therefore, when adding it,
It should be kept below 15%, preferably 0.07%
It is below, and particularly preferably less than 0.04%.

Ni is a very effective element for enhancing the toughness and preventing the formation of δ-ferrite.
If it is less than 5%, the effect is not sufficient, and if it exceeds 1.0%, the creep rupture strength is lowered, which is not preferable. Particularly, it is preferably 0.3 to 0.7%, more preferably 0.4 to 0.65%.

Cr is an essential element for enhancing the high temperature strength and the high temperature oxidation resistance, and at least 9% is necessary, but 13%
If it exceeds 0.1%, a harmful δ-ferrite structure is formed and the high temperature strength and toughness are reduced, so it is limited to 9 to 12%. Particularly, it is preferably 10 to 12%, more preferably 10.8 to 11.8%.

Mo is added to improve high temperature strength. However, in the case where the steel of the present invention contains more than 1% W, addition of 0.5% or more of Mo lowers the toughness and fatigue strength, so it is limited to 0.5% or less. Especially 0.05
.About.0.45%, more preferably 0.1 to 0.2%.

W suppresses the coagulation and coarsening of carbides at high temperatures, and solid-solution strengthens the matrix, and therefore has the effect of significantly increasing the high-temperature long-term strength at 620 ° C. or higher. 620
1 to 1.5% at ℃, 1.6 to 2.0% at 630 ℃, 6
2.1-2.5% at 40 ° C, 2.6-3.0 at 650 ° C
%, And at 660 ° C., it is preferably 3.1 to 3.5%.
Further, when W exceeds 3.5%, δ ferrite is formed and the toughness becomes low, so the content is limited to 1 to 3.5%. In particular, 2.4 to 3.0% is preferable, and 2.5 to 2.7% is more preferable.

V has the effect of precipitating carbonitrides of V to increase the creep rupture strength, but if it is less than 0.05%, the effect is insufficient, and if it exceeds 0.3%, δ ferrite is formed and the fatigue strength is increased. Lower. Particularly, 0.1 to 0.25% is preferable, and 0.15 to 0.23% is more preferable.

Nb is a very effective element for precipitating NbC carbides and increasing the high temperature strength. However, if added in a too large amount, coarse eutectic NbC carbides are produced, especially in large steel ingots, and the strength is rather increased. 0.2 because it causes the precipitation of δ-ferrite which lowers the fatigue strength.
It is necessary to suppress it to 0% or less. N less than 0.01%
In b, the effect is insufficient. Especially 0.02 to 0.15%
However, 0.04 to 0.10% is more preferable.

Co is an important element that distinguishes and characterizes the present invention from the prior art. In the present invention, addition of Co significantly improves high temperature strength and also enhances toughness. This is thought to be due to the interaction with W, and W
Is a characteristic phenomenon in the alloy of the present invention containing 1% or more. In order to realize such Co effect, the lower limit of Co in the alloy of the present invention is 2.0%. However, if added excessively, not only the larger effect cannot be obtained but also the ductility decreases. , The upper limit is 10%. Desirably 620
2-3% for ° C, 3.5-4 for 630 ° C.
5% to 5% to 640 ° C, 6.5% to 650 ° C to 7.5%, and 660 ° C to 8% to 9% are desirable.

N is also an important element that distinguishes and characterizes the present invention from the prior art. N is effective in improving creep rupture strength and preventing the formation of δ ferrite structure, but 0.0
If it is less than 1%, the effect is not sufficient, and if it exceeds 0.05%, toughness is lowered and creep rupture strength is also lowered. In particular, 0.01 to 0.03% is more preferable than 0.015%.
0.025% is preferable.

[0043] B is a solid solution in the grain boundary strength effects and M ₂₃ C ₆ carbide is effective to increase the high-temperature strength by the action preventing the aggregation and coarsening of M ₂₃ C ₆ type carbide, addition exceeding 0.001% Is effective, but if it exceeds 0.03%, the weldability and forgeability are impaired, so it is limited to 0.001 to 0.03%. Desirably 0.001 to 0.01%, or 0.01 to
0.02% is preferable.

The addition of Ta, Ti and Zr has the effect of increasing the toughness, and a sufficient effect can be obtained by adding Ta 0.15% or less, Ti 0.1% or less and Zr 0.1% or less alone or in combination. If Ta is added more than 0.1%, Nb
Can be omitted.

In the present invention, at least the first stage of the rotor shaft and the moving blades and the stationary blades have C0.09 to 0.20% and Si not more than 0.15% for a steam temperature of 620 to 630 ° C.
Mn 0.05 to 1.0%, Cr 9.5 to 12.5%, Ni 0.
1-1.0%, V0.05-0.30%, N0.01-0.0
6%, Mo 0.05-0.5%, W2-3.5%, Co2-
F of 4.5%, B0.001-0.030%, 77% or more
What is constituted by steel having a fully tempered martensitic structure with e is preferred. Also, 635-660
The above Co content is 5 to 8% with respect to the steam temperature of ℃,
It is preferably constituted by a steel having a fully tempered martensitic structure with 78% or more Fe. In particular, high strength can be obtained by reducing the Mn amount to 0.03 to 0.2% and the B amount to 0.001 to 0.01% with respect to both temperatures. In particular, C 0.09 to 0.20%, Mn 0.1
~ 0.7%, Ni 0.1-1.0%, V 0.10-0.30
%, N 0.02 to 0.05%, Mo 0.05 to 0.5%, W
2 to 3.5%, Co2 for 630 ° C or less
˜4%, B0.001-0.01% and 630-660 ° C., Co is preferably 5.5-9.0% and B0.01-0.03%.

The Cr equivalent calculated by the formula described below is preferably 4 to 10.5, particularly 6.5 to 9.5 for the rotor shaft, and the same is true for the others.

In the high-pressure and medium-pressure rotor material of the steam turbine of the present invention, if the δ ferrite structure is mixed, the fatigue strength and toughness are lowered, so that the structure is preferably a tempered martensite structure. In order to obtain a tempered martensite structure, the Cr equivalent calculated by the equation (1) must be 10 or less by adjusting the composition. If the Cr equivalent is too low, the creep rupture strength will decrease, so it must be 4 or more. Particularly, Cr equivalent of 5 to 8 is preferable.

In the rotor of the present invention, an alloy raw material having a target composition is melted in an electric furnace, carbon vacuum deoxidized, cast in a metal mold and forged to produce an electrode rod. The electrode rod is remelted by electroslag and forged into a rotor shape. This forging must be performed at a temperature of 1150 ° C. or lower in order to prevent forging cracks. Also, after this forged steel is annealed, it can be used in steam at 620 ° C or higher by quenching by heating to 1000 to 1100 ° C and quenching, and then tempering twice in the order of 550 to 650 ° C and 670 to 770 ° C. A steam turbine rotor can be manufactured.

The blade, nozzle, inner casing tightening bolt and intermediate pressure part first stage diaphragm in the present invention are melted by vacuum melting and cast in a mold under vacuum to manufacture an ingot. The ingot is hot forged into a predetermined shape at the same temperature as described above, heated at 1050 to 1150 ° C and then water-cooled or oil-quenched, and then tempered at 700 to 800 ° C, and a blade having a desired shape by cutting. Become. Vacuum melting is performed under 10 ^-1 to 10 ^-4 mmHg. In particular, the heat-resistant steel in the present invention can be used in all stages of the blade and nozzle in the high pressure region and the medium pressure region, but it is particularly necessary in the first stage of both.

In the steam turbine rotor shaft made of 12 wt% Cr martensitic steel in the present invention, it is preferable to form a build-up welding layer having high bearing characteristics on the surface of the base material forming the journal portion, and welding made of steel is performed. 5 to 10 layers of the overlay welding layer are formed by using a welding material, and the Cr content of the welding material from the first layer to any of the 2nd to 4th layers is sequentially decreased, and the 4th layer and subsequent layers Are welded using a welding material made of steel having the same Cr content, and the Cr content of the welding material used for the welding of the first layer is 2 from the Cr content of the base metal.
The amount of Cr is reduced to about 6 to 6% by weight, and the amount of Cr in the fourth and subsequent welding layers is set to 0.5 to 3% by weight (preferably 1 to 2.5% by weight).

In the present invention, the overlay welding is preferable for improving the bearing characteristics of the journal portion in terms of the highest safety, but the overlay welding becomes extremely difficult due to the increase in the amount of B in the steel. Therefore, B for higher strength
In order to make the content of 0.02% or more, it is preferable to have a structure in which a sleeve made of a low alloy steel having a Cr content of 1 to 3% is shrink-fitted and fitted. The composition of the sleeve is the same as the composition of the overlay layer described below.

The overlay welding layer obtained by the method of the present invention is 5
It is necessary to have 10 to 10 layers. As described above, a sharp decrease in the Cr content in the first weld layer causes a high tensile residual stress,
Alternatively, since the amount of Cr as a welding material cannot be significantly reduced because it causes weld cracking, it is necessary to increase the number of weld layers and gradually reduce the amount of Cr.
Further, as the surface layer, it is necessary to secure a desired amount of Cr and a desired thickness thereof, so that it is necessary to make the number of layers to be 5 or more. Even if 10 or more layers are welded, no further effect can be obtained. As a large-scale structural material such as a steam turbine rotor shaft, it is necessary to form a desired composition and a desired thickness without being affected by the composition of the base material as the overlay welding layer. It is necessary to have a desired thickness of 3 layers and a desired property on it, and a required thickness of 2 layers or more. For example, a final finish of about 18 mm is required. In order to form such a thickness, five build-up welding layers are required even if the final finishing allowance by cutting is removed. It is preferable that the third and subsequent layers mainly have a tempered martensite structure and carbides are precipitated. In particular, as the composition of the fourth and subsequent welding layers, by weight, C
0.01-0.1%, Si 0.3-1%, Mn 0.3-1.
5%, Cr 0.5 to 3%, Mo 0.1 to 1.5% and the balance Fe is preferable.

Further, the overlay welding layer is one in which the Cr content is sequentially reduced from the first layer to any of the second to fourth layers. In overlay welding, the Cr content is gradually lowered for each layer. Welding with a rod does not cause the problem of reduced ductility of the first layer weld due to a large difference in the chromium content of the first layer weld,
It is possible to form a build-up weld layer having a desired composition without causing weld cracking. As a result, the present invention can form the build-up welded layer having high bearing characteristics as described above in the final layer without causing an extreme difference in the chromium content in the vicinity of the base material and the initial layer portion.

As a welding material applied to the first layer welding, the chromium content thereof is reduced by about 2 to 6% by weight from the chromium content of the base metal. When the amount of Cr in the welded material is set to a value lower than that of the base metal and is 2% or less, the amount of Cr in the overlay welding layer cannot be sufficiently reduced, and the effect is small. On the other hand, when the content is 6% or more, the amount of Cr in the base metal and the overlay welding layer is rapidly decreased, and the difference in the amount of Cr causes a difference in the coefficient of thermal expansion, resulting in the generation of high tensile residual stress or the occurrence of welding cracks. Cause. Since the higher Cr has a smaller coefficient of thermal expansion, the overlay welding layer having a lower Cr has a larger coefficient of thermal expansion than the base metal and a high tensile residual stress is formed after welding. Therefore, welding with a lower Cr steel has a high hardness due to high residual stress and causes weld cracking. Therefore, the Cr content of the welded material must be 6% or less, which is less than that of the base material. is there. By using such a welding material, the chromium content of the first layer weld is mixed with the base metal,
Only about 1 to 3% lower than that of the base metal, and good welding can be obtained.

In the method of the present invention, it is necessary to form the fourth and subsequent layers using a welding material made of steel having the same Cr content. In the overlay welding, the composition of the base metal is affected up to the third layer, but the composition of the overlay welding layers of the fourth and subsequent layers is formed only by the composition of the welding material used. It is possible to form a journal that satisfies the required characteristics. Therefore, as described above, since the overlay welding layer required for a large-scale structure as a steam turbine rotor shaft is about 18 mm, the alloy composition necessary for the final layer and the necessary and sufficient thickness for that composition are secured. Therefore, the fourth and subsequent layers are welded in two or more layers with a welding material having the same amount of Cr, so that a material satisfying the above-mentioned characteristics required for the journal portion can be formed with a sufficient thickness.

(2) Internal casing control valve box of high pressure and medium pressure steam turbine of the present invention, combination reheat valve box, main steam reed pipe, main steam inlet pipe, reheat inlet pipe, high pressure turbine nozzle box, middle The reasons for limiting the composition of the ferritic heat resistant steel constituting the pressure turbine first stage diaphragm, the high pressure turbine main steam inlet flange, the elbow, and the main steam stop valve will be explained.

In the ferritic heat-resistant cast steel casing material, especially by adjusting the Ni / W ratio to 0.25 to 0.75, an ultra-supercritical turbine high pressure and intermediate pressure inner casing of 621 ° C. and 250 kgf / cm ² or more is obtained. And main steam stop valve and control valve casing, 625 ℃, 1
A heat-resistant cast steel casing material having a creep rupture strength of 0 ⁵ h 9 kgf / mm ² or more and a room temperature impact absorption energy of 1 kgf-m or more can be obtained.

In the ferritic heat-resistant cast steel casing material of the present invention, in order to obtain high high temperature strength, low temperature toughness and high fatigue strength, the Cr equivalent calculated by each component (% by weight) of the following formula is set to 4 to 10 It is preferable to adjust.

Cr equivalent = Cr% + 6Si% + 4Mo% +
1.5W% + 11V% + 5Nb% -40C% -30N%
-30B% -2Mn% -4Ni% -2Co% Since the 12Cr heat resistant steel of the present invention is used in steam at 621 ° C or higher, it has a creep rupture strength of 9 kgf / mm ² or higher at 625 ° C, 10 ⁵ h, and room temperature impact. Absorbed energy 1kg
It must be fm or more. Furthermore, in order to ensure higher reliability, creep rupture strength of 10 kgf / mm ² or more at 625 ° C., 10 ⁵ h, room temperature impact absorption energy of 2 k
It is preferably at least gf-m.

C is 0.06% in order to obtain high tensile strength.
The above elements are necessary, but if the content exceeds 0.16%, the metal structure becomes unstable when exposed to high temperature for a long time and the long-term creep rupture strength is reduced, so 0.06 to 0.16
Limited to%. It is particularly preferably 0.09 to 0.14%.

N has the effect of improving the creep rupture strength and preventing the formation of the δ ferrite structure, but if it is less than 0.01%, the effect is not sufficient, and if it exceeds 0.1%, there is no significant effect. On the contrary, it reduces toughness and also creep rupture strength. In particular, 0.02 to 0.01% is preferable.

Mn is added as a deoxidizer,
The effect is achieved with a small amount of addition, and a large amount of addition of more than 1% lowers the creep rupture strength, especially in the range of 0.4 to 0.7.
% Is preferred.

Although Si is also added as a deoxidizing agent, Si deoxidizing is not required according to the steelmaking technology such as vacuum C deoxidizing method. Further, by lowering Si, there is an effect of preventing harmful δ ferrite structure generation. Therefore, when adding it, it is necessary to suppress it to 0.5% or less, especially 0.5%.
1 to 0.4% is preferable.

V has an effect of increasing the creep rupture strength, but if it is less than 0.05%, the effect is insufficient and 0.35%.
If it exceeds, δ ferrite is formed to reduce the fatigue strength. Particularly, 0.15 to 0.25% is preferable.

Nb is an element which is very effective in increasing the high temperature strength. However, if added in a too large amount, coarse eutectic Nb carbides are produced especially in a large steel ingot, which rather lowers the strength or increases the fatigue strength. It causes the precipitation of δ-ferrite, which lowers the temperature, so it must be kept to 0.15% or less.
Further, if the Nb content is less than 0.01%, the effect is insufficient. Especially in the case of large steel ingots, 0.02 to 0.1% is more than 0.04.
~ 0.08 is preferred. Ni is a very effective element for increasing the toughness and preventing the formation of δ ferrite, but if it is less than 0.2%, its effect is not sufficient, and if it exceeds 1.0%, the creep rupture strength is increased. Is lowered, which is not preferable. Particularly, 0.4 to 0.8% is preferable.

Cr has the effect of improving high strength and high temperature oxidation. When it exceeds 12%, it causes harmful δ-ferrite structure formation, and when it is less than 8%, the oxidation resistance to high temperature and high pressure steam becomes insufficient. Further, addition of Cr has an effect of increasing creep rupture strength, but excessive addition causes harmful δ ferrite structure generation and toughness reduction. Especially 8.
0 to 10%, more preferably 8.5 to 9.5%.

W has the effect of significantly increasing the high temperature long-term strength. When W is less than 1%, the effect is insufficient as a heat-resistant steel used at 620 to 660 ° C. Further, if W exceeds 4%, the toughness becomes low. 1.0-1.5 at 620 ° C
%, 1.6-2.0% at 630 ° C, 2.1 at 640 ° C
~ 2.5%, 2.6-3.0% for 650 ° C, 66
It is preferably 3.1 to 3.5% at 0 ° C.

W and Ni are correlated with each other, and Ni /
By setting the W ratio to 0.25 to 0.75, one having high strength and toughness can be obtained.

Mo is added to improve high temperature strength. However, in the case where the cast steel of the present invention contains more than 1% W, the addition of 1.5% or more of Mo lowers the toughness and fatigue strength, so 1.5% or less is preferable, and especially 0.4- 0.
8%, more preferably 0.55 to 0.70%.

The addition of Ta, Ti and Zr has the effect of increasing the toughness, and sufficient effects can be obtained by adding Ta 0.15% or less, Ti 0.1% or less and Zr 0.1% or less alone or in combination. If Ta is added in an amount of 0.1% or more, N
The addition of b can be omitted.

In the heat-resistant cast steel casing material of the present invention, if the δ ferrite structure is mixed, the fatigue strength and toughness are lowered, so that the structure is preferably a tempered martensite structure. In order to obtain a tempered martensite structure, the Cr equivalent calculated by the equation (1) must be 10 or less by adjusting the composition. If the Cr equivalent is too low, the creep rupture strength will decrease, so it must be 4 or more. Particularly, Cr equivalent of 6 to 9 is preferable.

Addition of B markedly increases the creep rupture strength at high temperature (620 ° C. or higher). If the B content exceeds 0.003%, the weldability deteriorates, so the upper limit is limited to 0.003%. In particular, the upper limit of the B content of the large casing is 0.0028%, preferably 0.0005 to 0.0025%, and more preferably 0.001 to 0.002%.

Since the casing covers high-pressure steam at 620 ° C. or higher, high stress due to internal pressure acts. Therefore, from the viewpoint of preventing creep fracture, 10 ⁵ h creep rupture strength of 10 kgf / mm ² or more is required. Further, at the time of start-up, thermal stress acts when the metal temperature is low, and therefore room temperature impact absorption energy of 1 kgf-m or more is required from the viewpoint of preventing brittle fracture. On the higher temperature side, strengthening can be achieved by containing 10% or less of Co. In particular, 1 to 2% for 620, 2.5 to 3.5% for 630 ° C, 4 to 5% for 640 ° C, 6
It is preferably 5.5 to 6.5% at 50 ° C and 7 to 8% at 660 ° C.

To produce a casing with few defects,
Since the weight of the ingot is about 50 tons, it requires a high level of manufacturing technology. The ferritic heat-resistant cast steel casing material of the present invention can be made sound by melting an alloy raw material having a target composition in an electric furnace, refining it with a ladle, and then casting it into a sand mold. By performing sufficient refining and deoxidation before casting, it is possible to reduce casting defects such as shrinkage cavities.

In addition, the above cast steel is heated to 1000 to 1150 ° C.
A steam turbine that can be used in steam at 621 ° C or higher by performing normalizing heat treatment in which it is heated to 1000 to 1100 ° C and then rapidly cooled, and then tempered twice in the order of 550 to 750 ° C and 670 to 770 ° C. A casing can be manufactured.
If the annealing and normalizing temperature is 1000 ° C. or less, carbonitride cannot be sufficiently dissolved, and if it is too high, it causes coarsening of crystal grains. Further, the double tempering can completely decompose the retained austenite and form a uniform tempered martensite structure. A steam turbine that can be used in steam at 620 ° C. or higher by producing it by the above-mentioned manufacturing method can obtain a creep rupture strength of 10 kgf / mm ² or higher at 625 ° C. for 10 ⁵ h and a room temperature impact absorption energy of 1 kgf-m or higher. Can be a casing.

The casing in the present invention has the above-mentioned Cr equivalent and the amount of δ ferrite is preferably 5% or less, more preferably 0%.

The inner casing for the medium-pressure steam turbine is preferably made of forged steel in addition to the cast steel.

(3) Others (a) The low-pressure steam turbine rotor shaft is C by weight.
0.2-0.3%, Si 0.1% or less, Mn 0.2% or less,
Ni 3.2-4.0%, Cr 1.25-2.25%, Mo
A low alloy steel having a fully tempered bainite structure having 0.1 to 0.6% and V0.05 to 0.25% is preferable, and is preferably manufactured by the same manufacturing method as the high pressure and medium pressure rotor shafts described above. . Especially, the amount of Si is less than 0.05%, M
n 0.1% or less, other than P, S, As, Sb, Sn, etc., the raw material is made to be as low as possible, and the total amount is 0.025% or less. It is preferable to carry out the production.
P and S are preferably 0.010% or less, Sn and As are 0.005% or less, and Sb is 0.001% or less.

(B) Except for the final stage of the blade for the low-pressure turbine and the nozzle, C0.05-0.2%, Si0.1-0.1%.
5%, Mn 0.2-1.0%, Cr 10-13%, Mo 0.
Fully tempered martensitic steel with 04-0.2% is preferred.

(C) C0.2-0.3%, Si0.3-0.7%, M for both the inner and outer casings for the low-pressure turbine
Carbon cast steel with n1% or less is preferred.

(D) Main steam stop valve casing and steam control valve casing are C0.1-0.2%, Si0.1-0.4.
%, Mn 0.2 to 1.0%, Cr 8.5 to 10.5%, Mo
0.3-1.0%, W1.0-3.0%, V0.1-0.3
%, Nb 0.03 to 0.1%, N 0.03 to 0.08%, B
A fully tempered martensitic steel containing 0.0005 to 0.003% is preferred.

(E) T as the final stage rotor blade of the low pressure turbine
i alloy is used, in particular Ti with Al 5-8 wt% and V 3-6 wt% for lengths over 40 inches.
The longer the alloy is, the higher the content thereof can be used. Especially at 43 inches, Al
5.5-6.5%, V3.5-4.5%, 46-inch high strength material having Al4-7%, V4-7% and Sn1-3% is preferable.

(F) The outer casing for high and medium pressure steam turbines has C0.05 to 0.20% and Si0.05 to 0.5.
5%, Mn 0.1-1.0%, Ni 0.1-0.5%, Cr
1 to 2.5%, Mo 0.5 to 1.5%, V 0.1 to 0.3%, preferably B 0.001 to 0.01% and Ti 0.
It is preferable to manufacture by a cast steel containing at least one of 2% or less and having a fully tempered bainite structure.

[0084]

BEST MODE FOR CARRYING OUT THE INVENTION (Embodiment 1) A steam temperature 600 ° C. to 649 ° C. pulverized coal direct combustion boiler and a steam turbine are required in order to improve thermal efficiency by improving steam conditions, triggered by a fuel soaring after an oil shock. It Table 1 shows an example of such a steam-conditioning boiler.

[0085]

[Table 1]

Since steam oxidation occurs with such an increase in temperature, 8-10% is used instead of the conventional 2.25% Cr steel.
When Cr steel is used, the maximum sulfur content is 1% and the maximum chlorine content is 0.1% against high temperature corrosion due to pulverized coal direct combustion gas.
A material containing r of 20 to 25% and Ni of 20 to 35% and a trace amount of 0.5% or less of Al, Ti and Mo of 0.5 to 3%, and more preferably Nb of 0.5% or less is used. Since pulverized coal direct combustion results in high-temperature combustion, in order to reduce NOx, the combustion flame of primary air and pulverized coal and the inner peripheral air that forms a reducing flame on the outer periphery and the secondary air to the outer periphery are sent to achieve higher temperature. It is desirable to use a burner that creates a flame.

With the increase in capacity, the pulverized coal combustion furnace became larger, and the furnace width was 1050 MW, the furnace width was 31 m, and the furnace depth was 16 mm.
m, 1400 MW class, furnace width 34 m, furnace depth 18 m
Becomes

Table 2 shows the main specifications of a 1050 MW steam turbine with a steam temperature of 625 ° C. In this embodiment, the final stage blade length in the cross-compound type four-flow exhaust, low-pressure turbine is 43 inches, and HP-IP is 3600 r / min.
And LP2 have a rotation speed of 1800 r / min, and are composed of the main materials shown in the table in the high temperature part. The steam temperature in the high pressure part (HP) is 625 ° C and the pressure is 250 kg / cm ² , and the steam temperature in the intermediate pressure part (IP) is heated to 625 ° C by the reheater, and the pressure is 170 to 180 kg / cm ² . Be driven. The low-pressure part (LP) enters at a steam temperature of 450 ° C. and is sent to a condenser at a temperature of 100 ° C. or less and a vacuum of 722 mmHg.

[0089]

[Table 2]

FIG. 1 is a sectional view of the high pressure steam turbine. The high-pressure steam turbine is provided with a high-pressure axle (high-pressure rotor shaft) 23 in which a high-pressure rotor blade 16 is planted in a high-pressure inner casing 18 and a high-pressure outer casing 19 outside thereof. The above-mentioned high-temperature and high-pressure steam is obtained by the above-mentioned boiler, passes through the main steam pipe, passes through the main steam inlet 28 from the flange and elbow 25 constituting the main steam inlet, and is guided from the nozzle box 38 to the first-stage double-flow moving blades. Get burned. The first stage is a double flow, and the other side has 8
It is provided with steps. A stationary blade is provided corresponding to each of these moving blades. The rotor blade is a saddle type dovetail type, double tinon,
First stage wing length is about 35 mm. Length between axles is about 5.25 m
Also, the diameter of the smallest portion corresponding to the vane portion is about 620 mm, and the ratio of the length to the diameter is about 8.5.

The widths of the rotor blade implantation portions of the first stage and the last stage of the rotor shaft are substantially equal, and the stages are stepwise according to the downstream side in the second stage, the third to fifth stages, the sixth stage, and the seventh to eighth stages. It is smaller, and the axial width of the second implant is 0.64 times that of the final implant.

In the portion of the rotor shaft corresponding to the stationary blade, the diameter of the rotor shaft is smaller than that of the moving blade embedded portion. The axial width of that portion is gradually reduced from the width between the second-stage rotor blade and the third-stage rotor blade to the width between the final-stage rotor blade and the rotor blade in front of it. The width of the latter is 0.86 times smaller than the width of the former. Second stage ~
The size is reduced in two steps, up to the sixth step and from the sixth step to the ninth step.

In this example, the materials shown in Table 3 to be described later were all made of 12% Cr type steel containing no W, Co and B except that the first stage blade and nozzle were used. The length of the blade portion of the moving blade in this embodiment is 35 to 50 mm in the first stage and becomes longer in each stage from the second stage to the final stage, and particularly from the second stage to the final stage depending on the output of the steam turbine. Is 65 to 210 mm,
The number of stages is 9 to 12, and the length of the blades in each stage is 1.10 to 1.15, which is the length that the downstream side is adjacent to the upstream side, and that ratio on the downstream side. Is gradually increasing.

The diameter of the implanted portion of the moving blade is larger than that of the portion corresponding to the stationary blade, and the width thereof is larger as the length of the blade portion of the moving blade is larger. The ratio of the width to the blade length of the moving blade is 0.65 to 0.95 from the second stage to the final stage, and gradually decreases from the second stage to the final stage.

Further, the width of the rotor shaft in the portion corresponding to each vane is gradually reduced in each stage from the second stage and the third stage to the final stage and the front thereof. The ratio of the width to the blade length of the moving blade is 0.7 to 1.7, and becomes smaller from the upstream side to the downstream side.

FIG. 2 is a sectional view of the medium pressure steam turbine.
The medium-pressure steam turbine rotates the generator discharged together with the high-pressure steam turbine with the steam discharged from the high-pressure steam turbine to 625 ° C again by the reheater, and is rotated at a rotation speed of 3600 times / min. . The medium-pressure turbine has a medium-pressure inner casing 21 and an outer casing 22 similarly to the high-pressure turbine, and is provided with stationary vanes opposed to the medium-pressure rotor blade 17. The rotor blade 17 has two stages in six stages, and is provided on the left and right substantially symmetrically with respect to the longitudinal direction of the medium pressure axle (medium pressure rotor shaft). The distance between the bearing centers is about 5.5m,
The first stage blade length is about 92 mm and the last stage blade length is about 235 mm.
Dovetail is a reverse chestnut type. The diameter of the rotor shaft corresponding to the stationary blade before the final stage rotor blade is about 630 mm, and the ratio of the distance between the bearings to the diameter is about 8.7 times.

In the rotor shaft of the medium-pressure steam turbine of this embodiment, the axial width of the blade impregnating portion is gradually increased in three stages from the first stage to the fourth stage, the fifth stage, and the final stage.
The width at the final stage is about 1.4 times larger than that at the first stage.

In the rotor shaft of this steam turbine, the diameter corresponding to the stationary blade portion is small, and the width thereof is stepwise in four stages according to the first-stage rotor blade, the second-third stage and the last-stage rotor blade side. The width of the latter in the axial direction is about 0.7 times smaller than that of the former.

In this embodiment, the materials shown in Table 3 described later are used for the first stage blade and nozzle, and 12% Cr steel containing no W, Co and B is used. The length of the blade portion of the moving blade in this embodiment becomes longer in each stage from the first stage to the last stage, and the length from the first stage to the last stage is 90 to 350 mm depending on the output of the steam turbine, and the length from 6 to
In the 9 stages, the length of the blades in each stage is such that the downstream side is adjacent to the upstream side at a rate of 1.1 to 1.2.

The diameter of the implanting portion of the moving blade is larger than that of the portion corresponding to the stationary blade, and the width is larger as the blade length of the moving blade is larger. The ratio of the width to the blade length of the blade is 0 from the first stage to the last stage.
It is 5 to 0.7, and gradually decreases from the first stage to the last stage.

Further, the width of the rotor shaft in the portion corresponding to each vane is gradually reduced in each stage from the first stage and the second stage to the final stage and the front thereof. The ratio of the width to the blade length of the moving blade is 0.5 to 1.5 and becomes smaller from the upstream side to the downstream side.

FIG. 3 is a sectional view of the low pressure turbine. The low pressure turbines are connected in two tandems and have the same structure. Each of the moving blades 41 has eight stages on the left and right, and is substantially symmetrical to the left and right, and a stationary blade 42 is provided corresponding to the moving blades. The blade length of the final stage is 43 inches, Ti-based alloy is used, both have double tinon and saddle type dovetail, and the nozzle box 44 is a double flow type. The Ti-based alloy is age-hardened and contains 6% Al and 4% V by weight. The rotor shaft 43 is made of Ni 3.75%,
Cr 1.75%, Mo 0.4%, V 0.15%, C 0.25
%, Si 0.05%, Mn 0.10%, and a forged steel having a fully tempered bainite structure of a super clean material composed of residual Fe is used. 12% Cr steel containing 0.1% Mo is used for the moving blades and the stationary blades other than the last stage. For the inner and outer casing materials, C0.25% cast steel is used. The center distance of the bearing 43 in this embodiment is 750.
At 0 mm, the diameter of the rotor shaft corresponding to the vane is about 1
280 mm, the diameter at the blade-implanted part is 2275 mm.
The distance between the bearing centers for this rotor shaft diameter is about 5.9.

In the low-pressure turbine of the present embodiment, the axial width of the blade-implanted portion is from the first stage to the third stage, the fourth stage, the fifth stage, the sixth stage to the seventh stage, and the eighth stage.
The width of the last stage gradually increases in four stages, and the width of the last stage is about 2.5 times larger than the width of the first stage.

Further, the diameter of the portion corresponding to the stationary blade portion is small, and the axial width of that portion is gradually increased in the three stages of the fifth, sixth and seventh stages from the first stage moving blade side. The width of the final stage is about 1.9 times larger than that of the first stage.

The blade length of the rotor blade in this embodiment becomes longer in each stage from the first stage to the last stage, and the length from the first stage to the last stage is 90 to 12 depending on the output of the steam turbine.
The blade length of each stage is 70 to 70 mm, and the length of the blades in each stage is 1.3 to 1.6 times as long as the downstream side is adjacent to the upstream side.

The diameter of the implanting portion of the moving blade is larger than that of the portion corresponding to the stationary blade, and the width of the implanting portion is larger as the blade length of the moving blade is larger. The ratio of the width to the blade length of the blade is 0 from the first stage to the last stage.
It is 15 to 0.91 and gradually decreases from the first stage to the last stage.

Further, the width of the rotor shaft in the portion corresponding to each vane is gradually reduced in each stage from the first stage and the second stage to the final stage and the front thereof. The ratio of the width to the blade length of the moving blade is 0.25 to 1.25 and becomes smaller from the upstream side to the downstream side.

In addition to this embodiment, the steam inlet temperature to the high-pressure steam turbine and the medium-pressure steam turbine is 610 ° C, and the steam inlet temperature to the two low-pressure steam turbines is 385 ° C.
A similar configuration can be applied to a large-capacity power plant.

FIG. 4 shows a typical plant construction diagram of a coal burning high temperature and high pressure steam turbine plant.

The high-temperature and high-pressure steam turbine plant in this embodiment is mainly a coal-fired boiler 51 and a high-pressure turbine 5.
2, medium pressure turbine 53, low pressure turbine 54, low pressure turbine 55, condenser 56, condensate pump 57, low pressure feed water heater system 58, deaerator 59, booster pump 60, feed water pump 6
1, a high pressure feed water heater system 63 and the like.
That is, the ultra-high temperature high-pressure steam generated in the boiler 51 enters the high-pressure turbine 52 to generate power, and then the boiler 5 again.
It is reheated at 1 and enters the intermediate pressure turbine 53 to generate power. This medium-pressure turbine exhaust steam is used for the low-pressure turbine 5
4, 55, and after generating power, the condenser 56 condenses. This condensate is sent to the low pressure feed water heater system 58 and the deaerator 59 by the condensate pump 57. The feed water degassed by the deaerator 59 is sent to the high pressure feed water heater 63 by the booster pump 60 and the water feed pump 61 to be heated, and then the boiler 5
Return to 1.

In the boiler 51, the feed water passes through the economizer 64, the evaporator 65, and the superheater 66 to become high-temperature and high-pressure steam. On the other hand, the boiler combustion gas that has heated the steam exits the economizer 64 and then enters the air heater 67 to heat the air. Here, to drive the water supply pump 61, a turbine for driving the water supply pump that operates with the extracted steam from the intermediate pressure turbine is used.

In the high-temperature and high-pressure steam turbine plant constructed as described above, the temperature of the feed water exiting the high-pressure feed water heater system 63 is inevitably higher than the feed water temperature in the conventional thermal power plant, so that it is inevitable. The temperature of the combustion gas leaving the economizer 64 in the boiler 51 is also much higher than that of the conventional boiler. For this reason, heat is recovered from the boiler exhaust gas so as not to lower the gas temperature.

In place of the present embodiment, the same high pressure turbine,
The medium pressure turbine and the two low pressure turbines are connected in tandem, and a tandem compound-type power generation plant in which one generator is rotated to generate power can be similarly configured. As in the present embodiment, in a generator having an output of 1050 MW, a higher-strength generator shaft is used. In particular, C 0.15 to 0.30%, Si 0.3.
1-0.3%, Mn 0.5% or less, Ni 3.25-4.5
%, Cr 2.05 to 3.0%, Mo 0.25 to 0.60%,
It has a fully tempered bainite structure containing V0.05-0.20% and has a room temperature tensile strength of 93 kg / mm ² or more, especially 100
kg / mm ² or more, 50% FATT below 0 ° C, especially -20
The temperature is preferably below ℃, the magnetization force at 21.2 KG is below 985 AT / cm, and the total amount of P, S, Sn, Sb and As as impurities is 0.025% or below,
The Ni / Cr ratio is preferably 2.0 or less.

FIG. 5 is a high pressure and FIG. 6 is a front view of a medium pressure turbine rotor shaft. The high-pressure turbine shaft has a structure in which eight stages of blades are planted around the first stage blade planting portion on the multistage side. The intermediate-pressure turbine shaft has multi-stage blades having left and right six-stage blade-implanted portions that are substantially symmetrical, with the center being the boundary. Although the low-pressure turbine rotor shaft is not shown, a center hole is provided in each of the high-pressure, medium-pressure, and low-pressure turbine rotor shafts, and whether there is a defect through ultrasonic inspection, visual inspection, or fluorescent flaw detection through the center hole. Is inspected.

Table 3 shows the chemical composition (% by weight) used for the main parts of the high pressure turbine, the intermediate pressure turbine and the low pressure turbine of this embodiment. In the present embodiment, the high pressure and the medium pressure have a coefficient of thermal expansion of 12 × 10 ⁻⁶ / ° C., which has a ferrite-type crystal structure in all of the high temperature portions, so that there is no problem due to the difference in coefficient of thermal expansion. .

For the rotors of the high pressure part and the medium pressure part, 30 tons of heat resistant cast steel shown in Table 3 was melted in an electric furnace, carbon vacuum deoxidized, cast in a mold and forged to prepare an electrode rod. , Electroslag remelted so that this electrode rod melts from the upper part of cast steel to the lower part, rotor shape (diameter 1050m
m, length 3700 mm) was forged and molded. This forging was performed at a temperature of 1150 ° C. or lower in order to prevent forging cracks. Further, this forged steel was obtained by an annealing heat treatment, heating to 1050 ° C., quenching with water spray cooling, tempering twice at 570 ° C. and 690 ° C., and cutting into the shapes shown in FIGS. 5 and 6. In the present embodiment, the upper side of the electroslag steel ingot is the first-stage blade side and the lower side is the final-stage side.

For the blades and nozzles of the high pressure portion and the medium pressure portion, the heat resistant steels listed in Table 3 were also melted in a vacuum arc melting furnace to form the blade and nozzle material shape (width 150 mm, height 50 mm, length 1000 mm). Forged and molded. This forging was performed at a temperature of 1150 ° C. or lower in order to prevent forging cracks. Further, this forged steel is heated to 1050 ° C., oil-quenched, tempered at 690 ° C., and then cut into a predetermined shape.

Table 3 shows the inner casing of the high pressure part and the intermediate pressure part, the main steam stop valve casing and the steam control valve casing.
The heat-resistant cast steel described in 1 above was melted in an electric furnace, and after ladle refining, cast into a sand mold to produce. By performing sufficient refining and deoxidation before casting, it was possible to obtain a product having no casting defects such as shrinkage cavities. Weldability evaluation using this casing material is J
It carried out according to IS Z3158. The preheating, inter-pass and post-heating start temperatures were 200 ° C., and the post-heat treatment was 400 ° C. × 30 minutes. No weld crack was observed in the material of the present invention, and the weldability was good.

[0119]

[Table 3]

Table 4 shows the mechanical properties and heat treatment conditions obtained by cutting and investigating the main members of the high temperature steam turbine made of ferritic steel described above.

As a result of investigating the central portion of the rotor shaft, the characteristics required for the high-pressure and medium-pressure turbine rotor (62
It was confirmed that 5 ° C., 10 ⁵ h strength ≧ 13 kgf / mm ² , 20 ° C. shock absorption energy ≧ 1.5 kg-m) were sufficiently satisfied. This proves that a steam turbine rotor that can be used in steam at 620 ° C. or higher can be manufactured.

As a result of investigating the characteristics of this blade,
It was confirmed that the characteristics (625 ° C, 10 ⁵ h strength ≧ 15 kgf / mm ² ) required for the first stage blade of a high-pressure and medium-pressure turbine were sufficiently satisfied. This demonstrates that a steam turbine blade that can be used in steam at 620 ° C. or higher can be manufactured.

Further, as a result of investigating the characteristics of this casing, the characteristics (625 ° C., 10 ⁵ h strength ≧ 10 kgf / mm ² , 20 ° C. impact absorption energy ≧ 1 kg-m) required for high-pressure and medium-pressure turbine casings were sufficiently satisfied. It was confirmed that it was satisfactory and that welding was possible. This proves that a steam turbine casing that can be used in steam at 620 ° C. or higher can be manufactured.

[0124]

[Table 4]

FIG. 7 is a diagram showing the relationship between the 10 ⁵ hour breaking strength and the temperature of the rotor shaft material. It has been found that the material according to the invention meets the requirements of 610-640 ° C. The 12Cr rotor material is a conventional material containing no B, W and Co.

In this example, Cr-Mo low alloy steel was welded to the journal portion of the rotor shaft by overlay welding to improve the bearing characteristics. The overlay welding is as follows.

A coated arc welding rod (diameter 4.0φ) was used as the test welding rod. Table 5 shows the chemical composition (% by weight) of the deposited metal that was welded using the welding rod. The composition of the deposited metal is almost the same as the composition of the welding material.

The welding conditions are welding current 170A and voltage 24.
V, speed is 26 cm / min.

[0129]

[Table 5]

Overlay welding was carried out on the surface of the above-mentioned base metal as shown in Table 6 by combining the welding rods used for each layer to perform welding of 8 layers. The thickness of each layer was 3-4 mm, the total thickness was about 28 mm, and the surface was ground about 5 mm.

The welding conditions are preheating, interpass, stress relief annealing (SR) start temperature of 250 to 350 ° C., and SR treatment condition of 630 ° C. × 36 hours holding.

No. 1, No. 2 and 3 are all those of the present invention, and the composition of the fifth layer and thereafter is No. 1 shown in Table 6.
The composition was C and D.

[0133]

[Table 6]

In order to confirm the performance of the welded portion, overlay welding was similarly performed on the plate material and a side bending test at 160 ° was conducted, but no crack was observed in the welded portion.

Further, a bearing sliding test by rotation according to the present invention was carried out.
It was also excellent in oxidation resistance.

In place of this embodiment, a high pressure steam turbine, a medium pressure steam turbine and two low pressure steam turbines may be connected in tandem, and a tandem type power plant having 3600 rotations can be constructed in the same manner.

Example 2 An alloy having the composition shown in Table 7 was cast into a 10 kg ingot by vacuum induction melting, and
It is a forged square rod. In the case of a large steam turbine rotor shaft, 1050
℃ × 5 hours 100 ℃ / h cooling quenching, 570 ℃ × 20
Hour primary tempering and 690 ° C × 20 hour secondary tempering, and blade 1100 ° C × 1 hour quenching, 7
Tempering at 50 ℃ × 1 hour, 625 ℃, 30kgf
The creep rupture test was carried out at / mm ² . The results are also shown in Table 7.

From Table 7, the alloys of the present invention of No. 1 to No. 9 are
It can be seen that the creep rupture life is significantly longer than that of the No. 10 comparative alloy.

Of the comparative alloys, No. 10 is an alloy obtained by removing Co from the alloy of the present invention. FIG. 8 is a diagram showing the influence of Co amount on creep rupture strength, and FIG. 9 is a diagram showing the influence of B amount. As shown in the figure, the creep rupture time is improved as the amount of Co increases, but the increase in amount of Co is 600-
Since it tends to cause heat embrittlement when heated at 660 ° C., it is necessary to increase the strength and the toughness in the range of 620 to 630.
It is preferably 2 to 5% for ℃ and 5.5 to 8% for 630 to 660 ℃.

As shown in the figure, when the B content is increased, the strength tends to decrease, and it can be seen that the B content of 0.03% or less shows excellent strength. The amount of B is 0.0 at 620 to 630 ° C.
01-0.01% and Co content 2-4%, 630-66
On the higher temperature side of 0 ° C, the B content is set to 0.01 to 0.03%,
High strength can be obtained by increasing the amount of Co to 5 to 7.5%.

It was clarified that N was strengthened at a temperature higher than 600 ° C. in the example of the present application, and N was strengthened.
It became clear from the fact that o.2 has a higher strength than No. 8, which has a large amount of N. The N content is preferably 0.01 to 0.04%. Since N is hardly contained in the vacuum melting, it is added by the master alloy.

As shown in Table 7, it is apparent that the alloys according to the present invention show high strength as shown in FIG. 7 of Example 1. The rotor material shown in Example 1 is No. 1 of this example. It corresponds to the alloy of No. 2.

As shown in FIG. Mn amount of 8 is 0.
As is clear from the fact that those with a low content of 09% show a high strength when compared with the same amount of Co, M is required for further strengthening.
The n content is preferably 0.03 to 0.20%.

[0144]

[Table 7]

Example 3 Table 8 shows the chemical composition (% by weight) of the inner casing material of the present invention. As for the sample, assuming a thick part of a large casing, 200 kg is melted using a high frequency induction melting furnace, and the maximum thickness is 200 mm, width is 380 mm, and height is 4 mm.
It was cast in a sand mold of 40 mm to produce an ingot. Sample No.3〜
No. 7 is an invention material, and samples No. 1 and 2 are conventional materials.
Samples No. 1 and No. 2 are Cr-Mo-V cast steel and 11Cr-1Mo-V-Nb- used in the current turbine.
N cast steel. The sample was heat-treated (normalized / tempered) under the following conditions, assuming the thick portion of the large steam turbine casing, after the annealing treatment of 1050 ° C. × 8 h furnace cooling.

[0146] Weldability was evaluated according to JIS Z3158. The preheating, interpass and post-heating start temperatures were 150 ° C., and the post-heat treatment was 400 ° C. × 30 minutes.

[0147]

[Table 8]

Table 9 shows tensile properties at room temperature, V at 20 ° C.
Notch Charpy impact absorption energy, 650 ℃, 10
⁵ h creep rupture strength and weld crack test results are shown.

The creep rupture strength and impact absorption energy of the materials of the present invention (No. 3, 4, 6, 7) to which appropriate amounts of B, Mo and W are added have the characteristics (625 ° C. 10 ⁵ h strength ≧ 8 kgf / mm ² , 20
Satisfies the impact absorption energy of ℃ ≧ 1kg-m). Particularly, Nos. 3, 6 and 7 show high values of 9 kgf / mm ² or more. No welding cracks were observed in the material of the present invention,
Good weldability. As a result of investigating the relationship between the amount of B and weld cracking, when the amount of B exceeded 0.0035%, weld cracking occurred. There was a concern that the No. 3 one would break. Looking at the effect of Mo on mechanical properties, the amount of Mo is 1.18%
Many of them had a high creep rupture strength, but had a low impact value and could not satisfy the required toughness. On the other hand, M
In the case of 0.11%, although the toughness was high, the creep rupture strength was low and the required strength could not be satisfied.

As a result of investigating the influence of W on the mechanical properties, creep rupture strength is remarkably increased when the W content is 1.1% or more, but conversely, room temperature impact absorption energy is increased when the W content is 2% or more. Will be lower. Especially Ni / W ratio of 0.2
By adjusting to 5 to 0.75, the temperature of 621 ° C and the pressure of 250 kgf / cm ² or higher are required for the high-pressure and medium-pressure inner casing of the high-temperature high-pressure turbine, and the main steam stop valve and control valve casing. ⁵ h Creep rupture strength 9 kgf / mm ² or more, room temperature impact absorption energy 1 kgf-
A heat-resistant cast steel casing material of m or more is obtained. In particular, by adjusting the W amount of 1.2 to 2% and the Ni / W ratio to 0.25 to 0.75, the creep rupture strength of 625 ° C. and 10 ⁵ h is 1
0 kgf / mm ² or more, room temperature shock absorption energy 2 kgf-m
The above excellent heat-resistant cast steel casing material can be obtained.

[0151]

[Table 9]

FIG. 10 is a diagram showing the relationship between the W content and the creep rupture strength. As shown in the figure, when the W content is set to 1.0% or more, the strength is remarkably strengthened, and particularly at 1.5% or more, a value of 8.0 kg / mm ² or more is obtained.

FIG. 11 is a diagram showing the relationship between the 10 ⁵ hour breaking strength and the breaking temperature. No. 7 of the present invention sufficiently satisfied the required strength at 640 ° C or lower.

An alloy raw material having the target composition of the heat-resistant cast steel of the present invention was melted in an electric furnace in an amount of 1 ton, and after ladle refining, it was cast into a sand mold to obtain the inner casings of the high pressure portion and the intermediate pressure portion described in Example 1. It was

After the annealing heat treatment of the above cast steel at 1050 ° C. × 8 h furnace cooling, the normalizing heat treatment of 1050 ° C. × 8 h blow air cooling, 73
Two temperings of 0 ° C. × 8 h furnace cooling were performed. As a result of cutting and investigating this prototype casing having a fully tempered martensite structure, the characteristics required for a 250 atm, 625 ° C. high temperature and high pressure turbine casing (625 ° C., 10 ⁵ h strength ≧ 9 kgf
/ Mm ² , 20 ° C shock absorption energy ≧ 1 kg-m) was sufficiently satisfied and it was confirmed that welding was possible.

(Embodiment 4) In this embodiment, the steam temperatures of the high-pressure steam turbine and the intermediate-pressure steam turbine are set to those of Embodiment 1.
625 ° C. instead of 625 ° C., and the structure and size are obtained with substantially the same design as in Example 1. Here, what is different from the first embodiment is the rotor shaft of the high-pressure and medium-pressure steam turbine, the first-stage moving blades and the first-stage stationary blades, and the inner casing which are in direct contact with this temperature. As for these materials excluding the inner casing, the B content is increased to 0.01 to 0.03% and the Co content to 5 to 7% among the materials shown in the above Table 7, and the inner casing material of Example 1 is used. W amount 2
By increasing the content to ˜3% and adding Co to 3%, there is a great merit that the required strength is satisfied and the conventional design can be used. That is, in the present embodiment, the conventional design concept can be used as it is because all the structural materials exposed to high temperature are made of ferritic steel. still,
Since the steam inlet temperature of the second stage moving blade and the stationary blade is about 610 ° C., it is preferable to use the material used in the first stage of Example 1 for these.

Further, the steam temperature of the low-pressure steam turbine is about 405 ° C., which is slightly higher than the temperature of about 380 ° C. of the first embodiment.
As the rotor shaft itself, the material of Example 1 has sufficiently high strength, and thus a super clean material is also used.

Further, in the tandem type in which all are directly connected to the cross compound type in this embodiment, 3600 rpm
It can also be implemented at the number of revolutions.

[0159]

EFFECTS OF THE INVENTION According to the present invention, martensitic heat-resistant and cast steel having high creep rupture strength and room temperature toughness at 610 to 660 ° C. can be obtained. It can be made of heat-resistant steel, and the basic design of steam turbines up to now can be used as it is, resulting in a highly reliable thermal power plant.

Conventionally, at such a temperature, an austenitic alloy had to be used, and therefore a large large rotor could not be manufactured from the viewpoint of manufacturability. It is possible to manufacture various large rotors.

Further, since the all-ferritic steel high temperature steam turbine of the present invention does not use an austenitic alloy having a large coefficient of thermal expansion, the turbine can be rapidly started easily and is less susceptible to thermal fatigue damage. There are advantages.

[Brief description of drawings]

FIG. 1 is a sectional structural view of a ferritic steel high-pressure steam turbine according to the present invention.

FIG. 2 is a sectional structural view of a ferritic steel medium-pressure steam turbine according to the present invention.

FIG. 3 is a sectional structural view of a low-pressure steam turbine according to the present invention.

FIG. 4 is a configuration diagram of a coal burning power generation plant according to the present invention.

FIG. 5 is a sectional view of a rotor shaft for a high-pressure steam turbine according to the present invention.

FIG. 6 is a sectional view of a rotor shaft for a medium-pressure steam turbine according to the present invention.

FIG. 7 is a diagram showing the creep rupture strength of a rotor shaft material.

FIG. 8 is a graph showing the relationship between creep rupture time and Co content.

FIG. 9 is a graph showing the relationship between creep rupture time and B content.

FIG. 10 is a graph showing the relationship between creep rupture strength and W content.

FIG. 11 is a diagram showing the creep rupture strength of a casing material.

[Explanation of symbols]

1 ... 1st bearing, 2 ... 2nd bearing, 3 ... 3rd bearing, 4 ... 4th
Bearing, 5 ... Thrust bearing, 10 ... First shaft packing, 1
1 ... 2nd shaft packing, 12 ... 3rd shaft packing, 13 ... 4th shaft packing, 14 ... High pressure partition plate, 1
5 ... Medium pressure diaphragm, 16 ... High pressure blade, 17 ... Medium pressure blade, 18
... High-pressure inner compartment, 19 ... High-pressure outer compartment, 20 ... Medium-pressure inner first compartment, 21 ... Medium-pressure inner second compartment, 22 ... Medium-pressure outer compartment, 23 ... High-pressure axle, 24 ... Medium-pressure Axle, 25 ... Flange, Elbow, 26 ... Front bearing box, 27 ... Journal part,
28 ... Main steam inlet, 29 ... Reheat steam inlet, 30 ... High pressure steam exhaust port, 31 ... Cylinder connecting pipe, 38 ... Nozzle box (high pressure first stage), 39 ... Thrust bearing wear blocking device, 40 ...
Warm-up steam inlet, 51 ... Boiler, 52 ... High-pressure turbine, 5
3 ... Medium-pressure turbine, 54, 55 ... Low-pressure turbine, 56 ...
Condenser, 57 ... Condensate pump, 58 ... Low pressure feed water heater system, 59 ... Deaerator, 60 ... Booster pump, 61 ... Water feed pump, 63 ... High pressure feed water heater system, 64 ... Charcoal saver, 65 ...
Evaporator, 66 ... Superheater, 67 ... Air heater, 68 ... Generator.

─────────────────────────────────────────────────── ─── Continuation of the front page (72) Nobuo Shimizu Inventor No. 1-1, 3-chome, Sachimachi, Hitachi, Ibaraki Prefecture Hitachi Ltd. Hitachi factory (72) Inventor Norio Yamada 7-1, Omika, Hitachi, Ibaraki No. 1 Hitachi Ltd. in Hitachi Research Laboratory (72) Inventor Mitsuo Kuriyama 7-1-1 Omika-cho, Hitachi-shi, Ibaraki Hitachi Ltd. Hitachi Research Institute (72) Inventor Takao Hidaka Omika-cho, Hitachi City, Ibaraki Prefecture 7-1, 1-1 Hitachi Research Laboratory, Hitachi Research Laboratory (72) Inventor Shigeyoshi Nakamura 7-1, 1-1 Omika-cho, Hitachi City, Ibaraki Prefecture Hitachi Ltd. Hitachi Research Laboratory (72) Inventor Hiroshi Fukui Hitachi City, Ibaraki Prefecture 7-1-1 Omika-cho Hitachi Ltd. Hitachi Research Laboratory (72) Inventor Toshio Fujita Kanda, Chiyoda-ku, Tokyo 4-6, Surugadai Hitachi Ltd. (56) Reference JP 62-248806 (JP, A) JP 62-180044 (JP, A) JP 62-60845 (JP, A) JP 61-217554 (JP, A) JP 61-96026 (JP, A) JP 61-85502 (JP, A) JP 61-23749 (JP, A) JP 60-165358 (JP , A) JP 59-116360 (JP, A) JP 59-63305 (JP, A) JP 58-43303 (JP, A) JP 5-113106 (JP, A) JP 5-39702 (JP, A) JP-A-4-371551 (JP, A) JP-A-4-147948 (JP, A) JP-A-2-290950 (JP, A) (58) Fields investigated (Int. Cl. ⁷ , DB name) F01D 5/00 C22C 38/00 302 F01D 25/00

Claims (6)

(57) [Claims] 1. A rotor shaft, a rotor blade embedded in the rotor shaft, a stator blade for guiding the inflow of water vapor into the rotor blade, and an inner casing for holding the stator blade. The inlet temperature to the first stage of the moving blade is 610 to 660 ° C.
A steam turbine is, before all stages of kidou wing, Ri Do martensitic steel all stages and the inner casing of the stationary blade contains Cr8~13 wt%, the rotor shaft is heavy
Amount: C0.05-0.20%, Si 0.15% or less, M
n 0.05-1.5%, Cr 9.5-13%, Ni 0.05
~ 1.0%, V0.05 ~ 0.35%, Nb0.01 ~ 0.0.
20%, N 0.01 to 0.06%, Mo 0.05 to 0.5%
, W1.0-4.0%, Co2-10%, B0.0005
High strength, containing ~ 0.03% and having Fe of 78% or more
A steam turbine characterized by being made of martensitic steel . 2. The 10 ⁵ hour creep rupture strength at a temperature of the rotor shaft and at least the first stage of the moving blades and the stationary blades corresponding to the inlet temperature of the steam to the first stage of the moving blades is 1.
It is made of high-strength martensitic steel having a fully tempered martensite structure containing 9 to 13% by weight of Cr, which is 5 kg / mm ² or more, and the inner casing has a 10 ⁵ hour creep rupture strength at a temperature corresponding to the steam temperature. 10 kg
The steam turbine according to claim 1, wherein the steam turbine is made of a martensitic cast steel containing 8 to 12% by weight of Cr, which is not less than 1 / mm ² . At least the first stage wherein before Kidotsubasa and vanes weight, C0.05~0.20%, Si0.15% or less, Mn0.
03-1.5%, Cr 9.5-13%, Ni 0.05-1.
0%, V0.05 to 0.35%, Nb0.01 to 0.20
%, N 0.01 to 0.06%, Mo 0.05 to 0.5%, W
1.0-3.5%, Co2-10%, B0.0005-0.
Made of high-strength martensitic steel containing 03% and having at least 78% Fe, the inner casing being C by weight
0.06 to 0.16%, Si 0.5% or less, Mn 1% or less, Ni 0.2 to 1.0%, Cr 8 to 12%, V 0.05
~ 0.35%, Nb0.01 ~ 0.15%, N0.01 ~
0.1%, Mo1.5% or less, W1-4%, B0.000
The steam turbine according to claim 1 or 2, which is made of high-strength martensitic cast steel containing 5 to 0.003% and having 85% or more Fe. 4. A high-pressure turbine, the steam turbine power plant with a medium-pressure turbine and a low pressure turbine, the high pressure turbine and the intermediate pressure turbine Ri inlet temperature six hundred and ten to six hundred and sixty ° C. der to first stage rotor blade of the steam, It consists martensitic steel in which the high pressure turbine and all the stages of moving blades, wherein Ru is exposed to water vapor of the medium pressure turbine, all the stages and the inner casing of the stationary blade contains Cr8~13 wt%, the high data
The weight of the rotor and the rotor shaft of the medium-pressure turbine are C
0.05-0.20%, Si 0.15% or less, Mn 0.0
5 to 1.5%, Cr 9.5 to 13%, Ni 0.05 to 1.0
%, V0.05 to 0.35%, Nb 0.01 to 0.20
%, N 0.01 to 0.06%, Mo 0.05 to 0.5%,
W1.0-4.0%, Co2-10%, B0.0005-
High-strength material containing 0.03% and 78% or more Fe
A steam turbine power plant characterized by being made of lutensite steel . 5. A steam turbine power plant comprising a high-pressure turbine, a medium-pressure turbine, and two low-pressure turbines, wherein the high-pressure turbine and the medium-pressure turbine have a steam inlet temperature to a first stage moving blade of 610 to 660 ° C., and the low pressure. The turbine has a steam inlet temperature of 380 to 475 ° C. to the first-stage moving blade, and the metal temperature of the rotor blade of the high-pressure turbine and the metal temperature of the first-stage moving blade is steam to the first-stage moving blade of the high-pressure turbine. Keep the temperature below the inlet temperature by 40 ° C or less, and make sure that the metal temperature of the first stage rotor blade installation part and the first stage rotor blade of the rotor shaft of the intermediate pressure turbine is 75 ° C or more than the steam inlet temperature to the first stage rotor blade of the intermediate pressure turbine. All the stages of the moving blades of the high-pressure turbine and the intermediate-pressure turbine, all the stages of the stationary blades, and the inner casing are made of Cr9.5 so as not to go down.
Ri Do martensitic steel containing to 13% by weight,
The rotor shafts of the high-pressure turbine and the medium-pressure turbine are
By weight, C0.05 to 0.20%, Si 0.15% or less,
Mn 0.05-1.5%, Cr 9.5-13%, Ni 0.0
5 ~ 1.0%, V0.05 ~ 0.35%, Nb0.01 ~
0.20%, N 0.01 to 0.06%, Mo 0.05 to 0.
5%, W1.0-4.0%, Co2-10%, B0.00
High with Fe of 78% or more , including 05-0.03%
A steam turbine power plant characterized by being made of high- strength martensitic steel . 6. A coal-fired thermal power plant comprising a coal-fired boiler, a steam turbine driven by the steam obtained by the boiler, and a generator driven by the steam turbine and having a power generation output of 1000 MW or more by a single unit or two units. In the power plant, the steam turbine has a high-pressure turbine, a medium- pressure turbine, and two low-pressure turbines, and the high-pressure turbine and the medium-pressure turbine have a steam inlet temperature of 610 to 660 ° C. to the first-stage rotor blades and the In the low-pressure turbine, the steam inlet temperature to the first stage rotor blade is 380 to 450 ° C,
Steam heated to a temperature higher than the steam inlet temperature to the first-stage moving blades of the high-pressure turbine by the superheater of the boiler flows into the first-stage moving blades of the high-pressure turbine, and steam that has left the high-pressure turbine is reheated in the boiler. By heating the steam to a temperature higher than the steam inlet temperature to the first-stage moving blades of the intermediate-pressure turbine and flowing into the first-stage moving blades of the medium-pressure turbine, the steam discharged from the medium-pressure turbine is saved by the boiler economizer. said heating to a temperature above the steam inlet temperature to the first-stage moving blade of the low pressure turbine is flowed to the first stage moving blade of the low pressure turbine, all the stages of the rotor blades of the high pressure turbine and the intermediate pressure turbine, all the stages of the stationary blade and Inner casing is Cr 9.5-13
Ri Do martensitic steel containing by weight%, the high pressure
The rotor shaft of the turbine and medium-pressure turbine is heavy,
C0.05 to 0.20%, Si 0.15% or less, Mn0.2.
05-1.5%, Cr 9.5-13%, Ni 0.05-1.
0%, V0.05 to 0.35%, Nb 0.01 to 0.20
%, N 0.01 to 0.06%, Mo 0.05 to 0.5%,
W1.0-4.0%, Co2-10%, B0.0005-
High-strength material containing 0.03% and 78% or more Fe
A coal-fired thermal power plant characterized by being made of lutensite steel .