JPS6183802A - Boiler boosting controller - Google Patents
Boiler boosting controllerInfo
- Publication number
- JPS6183802A JPS6183802A JP20549984A JP20549984A JPS6183802A JP S6183802 A JPS6183802 A JP S6183802A JP 20549984 A JP20549984 A JP 20549984A JP 20549984 A JP20549984 A JP 20549984A JP S6183802 A JPS6183802 A JP S6183802A
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- JP
- Japan
- Prior art keywords
- pressure
- boiler
- steam
- stress
- thermal stress
- Prior art date
- Legal status (The legal status is an assumption and is not a legal conclusion. Google has not performed a legal analysis and makes no representation as to the accuracy of the status listed.)
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- Control Of Steam Boilers And Waste-Gas Boilers (AREA)
Abstract
(57)【要約】本公報は電子出願前の出願データであるた
め要約のデータは記録されません。(57) [Summary] This bulletin contains application data before electronic filing, so abstract data is not recorded.
Description
【発明の詳細な説明】
〔発明の利用分野〕
本発明はボイラ昇圧制御装置に係り、特に過熱器の出口
ヘッダのコー十部に発生する熱応力を減少させて寿命消
費量を低減するボイラ昇圧制御装置に関するものである
。゛
〔発明の背景〕
近年急増する電力需要に応えるために大容量の火力発電
所が建設されているが、これらのボイラは部分負荷時に
おいても高い発電効率を得るために、超臨界圧から亜臨
界圧へ変圧運転を行なうことが要求されている。[Detailed Description of the Invention] [Field of Application of the Invention] The present invention relates to a boiler boost control device, and particularly to a boiler boost control device that reduces thermal stress generated in the cord section of the outlet header of a superheater and reduces life consumption. This relates to a control device. [Background of the Invention] Large-capacity thermal power plants have been constructed in recent years to meet the rapidly increasing demand for electricity.In order to obtain high power generation efficiency even during partial load, these boilers have to convert from supercritical pressure to subcritical pressure. It is required to perform variable pressure operation to critical pressure.
これは最近の電力需要の特徴として、原子力発ｎの伸び
と共に、負荷の最大と最小の差も増大し、火力発電はベ
ースロード用から負荷調整用へと移行する傾向にあるか
らである。This is because, as a feature of recent electricity demand, as nuclear power generation increases, the difference between maximum and minimum loads increases, and thermal power generation tends to shift from base load to load adjustment.
つまり、火力発電は、ボイラ負荷が常に全負荷で・運転
されるものは少なく、負荷を８０％負荷、５０％負荷、
２５％負荷へと負荷を上げ、下げして運転したり、運転
を停止するなど、いわゆる高Ｈ度起動停止ＣＤａｉｌｙ
５ｔａｒｔ ５ｔｏｐ 以下単にＤｓＳという）運転
を行なって中間負荷を担うのである。In other words, in thermal power generation, the boiler load is always operated at full load.There are few cases where the boiler load is always operated at full load.
So-called high-H start/stop CDaily, such as increasing the load to 25% load, lowering it, and stopping the operation.
5tart 5top (hereinafter simply referred to as DsS) operation to carry intermediate loads.
このように火力発電は部分負荷での運転が増えた場合、
負荷に応じて圧力を変化させて運転する、いわゆる全負
荷では超臨界圧域、部分負荷では亜臨界圧域で運転する
ＤＳＳ運転を行なうことによって、部分負荷での発電効
率を数％向上させることができる。In this way, if thermal power generation is operated at partial load,
By performing DSS operation, which operates by changing the pressure according to the load, operating in the supercritical pressure region at full load and in the subcritical pressure region at partial load, power generation efficiency at partial load can be improved by several percentage points. Can be done.
第２図は変圧運転強制貫流ボイラの概略系統図である。FIG. 2 is a schematic system diagram of a forced once-through boiler operated at variable pressure.
給水ポンプ１で昇圧された給水は給水管路２で給水加熱
器３で加熱された後、節炭器４に入り、予熱されて火炉
水冷壁５，６で熱吸収し、天井壁７、ケージ壁８で再び
熱吸収されて蒸発し、気水分離器９に流入する。The feed water pressurized by the feed water pump 1 is heated by the feed water heater 3 in the water supply pipe line 2, then enters the economizer 4, where it is preheated and absorbed by the furnace water cooling walls 5 and 6, and is then transferred to the ceiling wall 7 and the cage. Heat is absorbed again by the wall 8, evaporates, and flows into the steam/water separator 9.
気水分離器９で分離された給水は循環管路１０の再循環
ポンプ１１で昇圧され、再循環流量調整弁１２により火
炉水冷壁５，６を冷却するために必要な流量に調整され
、給水管路２の給水と合流する。The feed water separated by the steam water separator 9 is pressurized by the recirculation pump 11 in the circulation pipe 10, and adjusted to the flow rate necessary for cooling the furnace water cooling walls 5, 6 by the recirculation flow rate adjustment valve 12. It merges with the water supply of pipe line 2.
一方、気水分１ｗ器９のレベルは気水分Ｍ器水位制御弁
１３により調整され、気水分離器９で分離された蒸気は
一次過熱器バイパス管路１４、−大過熱器バイパス弁１
５を経てフラッシュタンク１６に導かれる。On the other hand, the level of the steam/moisture 1w device 9 is adjusted by the steam/moisture M device water level control valve 13, and the steam separated in the steam/water separator 9 is passed through the primary superheater bypass line 14 - the large superheater bypass valve 1.
5 and is led to a flash tank 16.
この導かれた流体はフラッシュタンク１６で気水分離さ
れ、液状流体はフラッシュタンクドレン弁１７を有する
液体戻し管路１８より復水器１９の源側に供給され、蒸
気状流体はフラッシュタンク蒸気ダンプ弁２０を有する
蒸気戻し管路２１より復水器１９の蒸気側に供給されそ
れぞれ回収される。復水器１９の蒸気側に供給されそれ
ぞれ回収される。This led fluid is separated into steam and water in a flash tank 16, the liquid fluid is supplied to the source side of the condenser 19 from a liquid return line 18 having a flash tank drain valve 17, and the vapor fluid is transferred to a flash tank steam dump. The steam is supplied to the steam side of the condenser 19 through a steam return line 21 having a valve 20 and recovered. They are supplied to the steam side of the condenser 19 and recovered.
この復水器１９で回収された復水は給水となって復水管
路２２より復水ポンプ２３で圧送されて脱気器２４に導
かれて、ここで脱気されその後再び給水管路２に導かれ
る。The condensate recovered in the condenser 19 becomes feed water and is pumped through the condensate pipe 22 by the condensate pump 23 and led to the deaerator 24, where it is deaerated and then returned to the water supply pipe 2. be guided.
他方、ケージ壁８の蒸気温度及び蒸気圧力が上昇するに
つれて発生蒸気の一部は蒸気供給管路２５を経て一次過
熱器２６に供給され、ここでさらに過熱された蒸気は二
次過熱器バイパス管路２７、二次過熱器バイパス弁２８
を経てフラッシュタンク１６へ導かれる。On the other hand, as the steam temperature and steam pressure on the cage wall 8 rise, a part of the generated steam is supplied to the primary superheater 26 via the steam supply pipe 25, and the steam further superheated here is supplied to the secondary superheater bypass pipe. passage 27, secondary superheater bypass valve 28
It is guided to the flash tank 16 through the.
また−次週熱器２６で加熱された蒸気は過熱器減圧弁２
９を経て二次過熱器６０で過熱され主蒸気管路３１へ供
給される。Also, the steam heated in the heater 26 next week will be transferred to the superheater pressure reducing valve 2.
9, is superheated in a secondary superheater 60, and is supplied to the main steam pipe line 31.
この様に主蒸気管路６１が暖まるまでは絞り弁３２が閉
じられて蒸気はタービンバイパス管路３３、ター１：”
ンバイパス弁６４を経てフラッシュタンク１６へ導かれ
る。In this way, the throttle valve 32 is closed until the main steam line 61 warms up, and the steam is transferred to the turbine bypass line 33 and the turbine 1.
is led to the flash tank 16 via a bypass valve 64.
その後に主蒸気管路３１が暖まると絞り弁６２をやや開
いてタービンバイパス弁６４を閉じて高圧タービン３５
へ蒸気を供給しタービン暖機運転に入る。After that, when the main steam line 31 warms up, the throttle valve 62 is slightly opened and the turbine bypass valve 64 is closed, and the high-pressure turbine 35
supply steam to the turbine and start turbine warm-up operation.
高圧タービン３５を出た蒸気は再熱器６６によって加熱
され、低圧タービン６７を経て排気管路６８より復水器
１９に導かれる。６９は脱気器加熱蒸気弁、４０はバー
ナ、４１は燃料調節弁である０
一方、二次過熱器６０の出口には第６図に示す様な出口
ヘッダ４０が取付けられ、ノズルコーナ部４１を有する
。Steam exiting the high-pressure turbine 35 is heated by a reheater 66, passes through a low-pressure turbine 67, and is guided to the condenser 19 via an exhaust pipe 68. 69 is a deaerator heating steam valve, 40 is a burner, and 41 is a fuel control valve.On the other hand, an outlet header 40 as shown in FIG. 6 is attached to the outlet of the secondary superheater 60, and the nozzle corner portion 41 is have
ところが、火力発電用ボイラの中間負荷運用化に伴ない
ＤＢＳ運転を行なうと、ボイラ耐圧部の厚肉管（二次過
熱器３０の出口ヘッダ４２のノズルコーナ部４３）に発
生する応力、およびこの応力に伴なう寿命消費が問題と
なる。However, when DBS operation is performed in conjunction with intermediate load operation of boilers for thermal power generation, stress occurs in the thick-walled tube of the boiler pressure-resistant section (nozzle corner portion 43 of the outlet header 42 of the secondary superheater 30), and this stress Life consumption associated with this becomes a problem.
特に、高温で高圧の蒸気にさらされる最終過熱器３０の
出口ヘッダ４２の７ズルフ一ナ部４３に発生する応力、
寿命消費はボイラプラントが要求される運用期間を信頼
性高く運用できるか否かの重要な評価基準になっている
。In particular, the stress generated in the inner part 43 of the outlet header 42 of the final superheater 30, which is exposed to high temperature and high pressure steam;
Lifetime consumption is an important evaluation criterion for whether a boiler plant can operate reliably for the required operating period.
最終過熱器３０の出口へラダ４２で消費される寿命の大
部分はクリープ損傷によるものである。Most of the life consumed in the ladder 42 to the exit of the final superheater 30 is due to creep damage.
以下このクリープ損傷評価法を第４図を用いて簡単に説
明する。This creep damage evaluation method will be briefly explained below using FIG. 4.
第４図は横軸に時間、縦軸に応力を示したボイラ起動時
の発生応力模式図である。FIG. 4 is a schematic diagram of the stress generated when the boiler is started, with time on the horizontal axis and stress on the vertical axis.
ボイラをコールドスタートで運転して停止したり、ある
いはウオームスタートで運転して停止したりの様に、運
転、停止を繰り返すと第３図の出口ヘッダ４２の中で最
も発生応力の大きいノズルコーナ部４６の応力は第４図
に示す様に変化する。When the boiler is repeatedly operated and stopped, such as when the boiler is operated with a cold start and then stopped, or when it is operated and stopped with a warm start, the nozzle corner portion 46 in the outlet header 42 shown in FIG. 3 has the largest stress. The stress changes as shown in FIG.
それは、ボイラ点人後、出口ヘッダ４２の流体温度上昇
とともに第４図のＡ点からＢ点では圧縮応力が発生し、
定常運転に移行するに従って第４図のＢ点から０点では
引張応力が発生する。この現象は、Ａ点からＢ点間では
熱応力、Ｂ点からＤ点間では熱応力に対して内圧応力が
優勢になっていることを表わしている。This is because after the boiler is turned on, compressive stress is generated from point A to point B in Fig. 4 as the fluid temperature in the outlet header 42 rises.
As the operation shifts to steady state, tensile stress is generated from point B to point 0 in FIG. This phenomenon indicates that thermal stress is dominant between points A and B, and internal pressure stress is dominant over thermal stress between points B and D.
ここで、蒸気温度が出口ヘッダ４１の材質により決まる
クリープ温度領域を越える所で、応力を保持していると
クリープ損傷による寿命を消費することになる。Here, if stress is maintained at a point where the steam temperature exceeds the creep temperature range determined by the material of the outlet header 41, the service life will be wasted due to creep damage.
第５図は縦軸に第４図の応力を示し、横軸にひずみを示
した応力、ひずみ特性曲線図で、第５図中の＾ゝ、Ｂ、
Ｏ，Ｄ点は第４図のＡ、Ｂ、Ｏ，Ｄ点と同一のものを示
す。Figure 5 is a stress/strain characteristic curve diagram in which the stress in Figure 4 is shown on the vertical axis and the strain is shown on the horizontal axis.
Points O and D are the same as points A, B, O and D in FIG.
クリープ損傷は、第４図、第５図の初期応力σｉとクリ
ープ保持時間により決まるが、第４図、第５図の初期応
力σ１ は、下式（１）で得られる。Creep damage is determined by the initial stress σi and creep holding time shown in FIGS. 4 and 5, and the initial stress σ1 shown in FIGS. 4 and 5 is obtained by the following formula (1).
ア
σｉ−（σｒ ＋ Ｙｔ） （−１）＋すτ・・・・・
（１）ここに、すｆ：定格運転時相当応力
σｆ ：圧縮最大相当応力 ゛
（マイナスは圧縮応力、プラスは
引張応力）
Ｅ、Ｆ：材質、温度により決る定数
Ｙ１：降伏応力
初期応力σｉ を抑えて、クリープ損傷を小さくしよう
とすれば（１）式のうち圧縮最大相当応力στ（第４図
、第５図のＢ点）の絶対値を抑えることが必要になる。Aσi−(σr + Yt) (−1)+suτ・・・・・・
(1) Here, f: Equivalent stress at rated operation σf: Maximum compressive equivalent stress (minus: compressive stress, plus: tensile stress) E, F: Constant determined by material and temperature Y1: Yield stress Initial stress σi In order to reduce the creep damage, it is necessary to suppress the absolute value of the maximum compressive equivalent stress στ (point B in FIGS. 4 and 5) in equation (1).
すなわち、前記（１）式で、定格運転は、材質、温度に
より決まるので直接制御することはできないからである
。That is, in the above equation (1), the rated operation is determined by the material and temperature and cannot be directly controlled.
第６図はボイラの連続運転時間（保持時間）を一定とし
たときの圧縮最大相当応力δζ と寿命消費率φの特性
曲線図で、目盛は両対数表示である０この第６図からク
リープ損傷は圧縮最大相当応力δζ に依存している。Figure 6 is a characteristic curve diagram of maximum compressive equivalent stress δζ and life consumption rate φ when the continuous operation time (holding time) of the boiler is constant, and the scale is logarithmic. depends on the maximum compressive equivalent stress δζ.
第７図は縦軸に蒸気圧力、蒸気温度を示し、横軸に時間
を示した起動時の蒸気圧力、蒸気温度の時間変化？示す
特性曲線図、第８図は縦軸に応力、横軸に時間を示し、
第７図の流体条件における過熱器６０における出口ヘッ
ダ４２のノズルコーナ部４３に発生する熱応力、内圧応
力の変化を示す特性曲線図である。In Figure 7, the vertical axis shows steam pressure and steam temperature, and the horizontal axis shows time. Changes in steam pressure and steam temperature over time at startup? The characteristic curve diagram shown in Figure 8 shows stress on the vertical axis and time on the horizontal axis,
8 is a characteristic curve diagram showing changes in thermal stress and internal pressure stress generated in the nozzle corner portion 43 of the outlet header 42 in the superheater 60 under the fluid conditions of FIG. 7. FIG.
なお、第７図において曲線Ｇは蒸気温度、曲線Ｈは蒸気
圧力、第８図において、曲線工は内圧応力、曲線Ｊは熱
応力を示し、ＴＩ−Ｔｓは時間を示す。In addition, in FIG. 7, the curve G shows the steam temperature, the curve H shows the steam pressure, and in FIG. 8, the curve line shows the internal pressure stress, the curve J shows the thermal stress, and TI-Ts shows the time.
従来のボイラ起動時におけるタービン通気（第７図、＃
！８図のＴ２）後、ボイラが再循環運転されている間（
第７図、ｔＪｓ図の’Ｉ’ｓ）の昇圧制御は主蒸気圧カ
一定の目標設定を行ない第２図に示すり・ −ビンバイ
パス弁３４を閉じるか、あるいは燃料調節弁４１を開い
て第７図の曲線Ｈ上に示すＫ。Turbine ventilation during conventional boiler startup (Fig. 7, #
! After T2 in Figure 8), while the boiler is in recirculation operation (
The pressure increase control of 'I's in the tJs diagram in Fig. 7 is performed by setting a constant target for the main steam pressure as shown in Fig. 2. K shown on curve H in FIG.
Ｌ、Ｍ、Ｎ点の様に主蒸気圧力を上げて制御していた。It was controlled by increasing the main steam pressure at points L, M, and N.
従って、変圧ペンソンボイラの最終過熱器３０の出口ヘ
ッダ４２に発生する応力を実運転データより解析すると
通気時Ｔ２ から低負荷時（循環運転時） Ｔａ
間において□は第８図の曲線Ｊで示す如く最大の圧縮相
当応力δζ が発生している。Therefore, when the stress generated in the outlet header 42 of the final superheater 30 of a transformer Penson boiler is analyzed from actual operation data, it varies from T2 during ventilation to Ta at low load (during circulation operation).
As shown by the curve J in FIG. 8, the maximum compressive equivalent stress δζ occurs in the area □.
この様にＴ２からＩＩＩ、においては第８図の曲線Ｊで
は圧縮応力がピークになり、曲線工では引張応力が一定
であり、圧縮最大相当応力δζ を低下させてクリープ
損傷による寿命消費を低減することはできない。
り
〔発明の目的〕
本発明はかかる従来の欠点を解消しようとするもので、
その目的とするところは、ボイラ起動時に過熱器の出口
ヘッダに発生する熱応力を減少して発生応力、寿命消費
を低減し、ボイラにおける信頼性の向上を計ることがで
きるざイラ昇圧制御装置を得ようとするものである。In this way, from T2 to III, compressive stress peaks at curve J in Figure 8, while tensile stress remains constant at curved lines, reducing the maximum compressive equivalent stress δζ and reducing life consumption due to creep damage. It is not possible.
[Object of the Invention] The present invention aims to eliminate such conventional drawbacks,
The objective is to develop a boiler boost control system that can reduce the thermal stress generated at the outlet header of the superheater when the boiler is started, thereby reducing the generated stress and life consumption, and improving the reliability of the boiler. That's what you're trying to get.
本発明は前述の目的を達成するために、実測値を基にボ
イラ耐圧部に発生する熱応力を予測する熱応力ピーク予
測器と、この熱応力ピーク予測器からの熱応力ピーク予
測値を基に主蒸気圧力を設定する主蒸気圧力設定器を設
け、主蒸気圧力設定器からの主蒸気圧力設定値と、主蒸
気圧力検出器からの主蒸気圧力実測値との偏差によって
ボイラ耐圧部の内圧を高めるようにしたものである。In order to achieve the above-mentioned object, the present invention provides a thermal stress peak predictor that predicts the thermal stress occurring in a boiler pressure section based on actual measurement values, and a thermal stress peak predictor based on the thermal stress peak predicted value from the thermal stress peak predictor. A main steam pressure setting device is installed to set the main steam pressure, and the internal pressure of the boiler pressure-resistant section is determined by the deviation between the main steam pressure set value from the main steam pressure setting device and the main steam pressure actual value from the main steam pressure detector. It was designed to increase the
以下本発明の実施例を図面を用いて説明する。 Embodiments of the present invention will be described below with reference to the drawings.
第１図は本発明の実施例に係るボイラの昇圧制御装置の
概略系統図である。FIG. 1 is a schematic system diagram of a boiler boost control device according to an embodiment of the present invention.
第１図において蒸気温度検出器４４により蒸気温度実測
値４５、蒸”気圧力検出器４６により蒸気圧力実測値４
７、蒸気流量検出器４８により蒸気流量実測値４９を検
出する。検出した実測値４５゜４７．４９をもとに、統
計モデルにより区間（第７図、第８図のＴ２〜Ｔｓ間）
内の時刻における流体条件を予測する。すなわち、蒸気
温度予測器５０において蒸気温度予測値５１、蒸気圧力
予測器５２において蒸気圧力予測値５３、蒸気流量予測
器５４において蒸気流量予測値５５が得られる。In FIG. 1, the steam temperature detector 44 indicates an actual steam temperature value 45, and the steam pressure detector 46 indicates an actual steam pressure value 4.
7. The steam flow rate detector 48 detects the actual steam flow rate value 49. Based on the detected actual measurement value of 45°47.49, the interval (between T2 and Ts in Figures 7 and 8) is calculated using a statistical model.
Predict fluid conditions at times within. That is, the steam temperature predictor 50 obtains a steam temperature predicted value 51, the steam pressure predictor 52 obtains a steam pressure predicted value 53, and the steam flow rate predictor 54 obtains a steam flow rate predicted value 55.
これら予測値５１．５３．５５の流体条件から流体から
熱伝達率演算器５６においてメタルへの熱伝達率演算値
５７を求める。これをもとに、非定常熱伝導方程式を解
いて管寄板厚方向温度外布を求める。Based on the fluid conditions of these predicted values 51, 53, and 55, a heat transfer coefficient calculation value 57 from the fluid to the metal is determined by a heat transfer coefficient calculation unit 56. Based on this, the unsteady heat conduction equation is solved to find the temperature distribution in the thickness direction of the header board.
例えば円筒の熱伝達方程式■および境界条件（３）、（
４）を解くことにより求める。For example, the heat transfer equation for the cylinder ■ and the boundary condition (3), (
It is obtained by solving 4).
工 １ “Ｔ１ｆｆ”Ｉ’ ・・・・・・・・・・・
・■α−τ−τ＝シ＋７１７ 。Engineering 1 “T1ff”I' ・・・・・・・・・・・・
・■α−τ−τ=shi+717.
Ｊ Ｃｌニーｈ（Ｔｔ Ｔｏ）’内面境界条件・・
・（６）α ｒ
ｃｒ Ｔ−ｏ 、外面境界条件・・・
Ａ）α ｒ
α：メタル温度伝導度 Ｔ：メタル温度６８時間
ｒ：円筒中心からの距離Ｔｆ：流体温度
Ｔ、：メタル内面温度この方程式■、（３）、（４）
を解いて求められた熱伝達率演算値５７を基に温度分布
演算器５８によって温度分布演算値５９を求める。J Cl knee h (Tt To)' inner boundary condition...
・(6) α r cr T−o, outer boundary condition...
A) α r α: Metal temperature conductivity T: Metal temperature 68 hours
r: Distance from cylinder center Tf: Fluid temperature
T: Metal inner temperature This equation ■, (3), (4)
A temperature distribution calculation value 59 is determined by a temperature distribution calculation unit 58 based on the heat transfer coefficient calculation value 57 obtained by solving the equation.
この温度分布演算値５９より、熱応力演算器６０におい
て熱応力演算値６１を求める。つぎに、熱応力演算値６
１を基に熱応力ピーク時刻予測器６２において、区間内
で最大の圧縮熱応力が発生する時刻を予測する。From this temperature distribution calculation value 59, a thermal stress calculation value 61 is determined by a thermal stress calculation unit 60. Next, the thermal stress calculation value 6
1, the thermal stress peak time predictor 62 predicts the time at which the maximum compressive thermal stress will occur within the section.
この様に蒸気温度予１１！Ｉ器５０、蒸気圧力予測器５
２、蒸気流量子１ｍ器５４、熱伝達率演算器５６、温度
分布演算器５８、熱応力演算器６Ｇおよび熱応力ピーク
時刻予測器６２によって熱応力ピーク予測器６３が構成
されている。In this way, the steam temperature is predicted to be 11! I device 50, steam pressure predictor 5
2. The thermal stress peak predictor 63 is composed of the steam flow rate 1m device 54, the heat transfer coefficient calculator 56, the temperature distribution calculator 58, the thermal stress calculator 6G, and the thermal stress peak time predictor 62.
この熱応力ピーク予測器６３からの熱応力ピーク予測値
６４に基し１て主蒸気圧力設定器６５において、その区
間（＃！７図、第８図のＴ１−Ｔｉ）での昇圧が、熱応
力ピーク発生時刻に一致するよう、主蒸気圧力設定を行
なう。Based on the predicted thermal stress peak value 64 from the thermal stress peak predictor 63, the main steam pressure setting unit 65 determines whether the pressure increase in that section (T1-Ti in Figures #!7 and 8) The main steam pressure is set to match the stress peak occurrence time.
この主蒸気圧力設定器６５で設定した主蒸気圧力設定値
６６と、蒸気圧力検出器４６で検出された蒸気圧力実測
値４７を一致させるために演算器６７によって偏差６８
を求め、この偏差６８を比例積分演算器６９に入れ、出
力信号７ｏを弁開度調節ｒＩ７１に与える制御信号７２
によってタービンバイパス弁３４を閉じるか、あるいは
燃料調節弁４１を開いて昇圧するのである。In order to match the main steam pressure setting value 66 set by the main steam pressure setting device 65 and the steam pressure actual value 47 detected by the steam pressure detector 46, the calculator 67 uses a deviation 68.
This deviation 68 is input to the proportional integral calculator 69, and the control signal 72 gives the output signal 7o to the valve opening adjustment rI71.
Accordingly, the turbine bypass valve 34 is closed or the fuel control valve 41 is opened to increase the pressure.
従来のボイラ起動時における昇圧制御は、前述した様に
タービンバイパス弁６４、燃料調節弁４１の弁操作はプ
ログラム制御により行なわれ、その目標圧力の設定は計
画時に決めたものを泪い変更されるものではなく第７図
の曲線Ｈで示す様にに、Ｌ、Ｍ点へと昇圧していた。In the conventional pressure increase control at the time of boiler startup, as mentioned above, the valve operations of the turbine bypass valve 64 and the fuel control valve 41 are performed by program control, and the target pressure setting is changed from that determined at the time of planning. Instead, the pressure increased to points L and M, as shown by curve H in Figure 7.
ところが、本発明においては、高温、高圧の蒸気にさら
される過熱器出口ヘッダ６０等のクリープ損傷による寿
命消費に大きく寄与する起動時の圧縮応力δ、に注目し
、目標圧力設定を行なうものでタービン通気時（第７，
８図のＴｚ）からボイラの再循環運転時（第７．８図の
Ｔｓ）間に第７図の破線Ｏで示す如く内圧をに、Ｐ、Ｍ
へと高くし、第８図の曲線Ｊで示す圧縮熱応力のピーク
に一致するように昇圧するのである。However, in the present invention, the target pressure is set by focusing on the compressive stress δ at startup, which greatly contributes to the life consumption due to creep damage of the superheater outlet header 60 etc. exposed to high temperature and high pressure steam. During ventilation (7th,
During the recirculation operation of the boiler (Ts in Figure 7.8), the internal pressure is changed to P, M as shown by the broken line O in Figure 7.
The pressure is increased to match the peak of compressive thermal stress shown by curve J in FIG.
第８図で昇圧時、圧縮熱応力ピークに昇圧を一致させた
場合、蒸気圧力は第７図の破線Ｏで示すように高くなる
が、内圧応力は第８図の破線Ｑで示すように低くなる。When increasing the pressure in Figure 8, if the pressure increase coincides with the compression thermal stress peak, the steam pressure will increase as shown by the broken line O in Figure 7, but the internal pressure stress will decrease as shown by the broken line Q in Figure 8. Become.
つまり、従来の昇圧装置では内圧応力は第８図の曲線■
（実線）で示す如く大きくなり、この時の昇正による熱
応力への影響は小さく、熱応力は第８図の曲線Ｊで示す
如く変らない。In other words, in the conventional pressure booster, the internal pressure stress is the curve shown in Figure 8.
(solid line), the influence of the increase on the thermal stress at this time is small, and the thermal stress does not change as shown by the curve J in FIG.
つぎに、過熱器３０における出口ヘッダ４２ノズル内面
コーナ部４３でのトータルの発生応力を見ると、本発明
のように昇圧させると圧縮の熱応力を引張の内圧応力で
相殺することになり、第４図および第５図における従来
の点Ａ、Ｂ、Ｏ，Ｄの実線は、本発明の点Ａ、Ｒ，８，
Ｔの破線の様になる。Next, looking at the total stress generated at the outlet header 42 nozzle inner corner portion 43 in the superheater 30, when the pressure is increased as in the present invention, the compressive thermal stress is offset by the tensile internal pressure stress. The solid lines of the conventional points A, B, O, and D in FIGS. 4 and 5 are the points A, R, 8, and 8 of the present invention.
It will look like the broken line of T.
従って、結果的には圧縮応力の絶対値を小さくすること
になり、クリープ寿命消費をそれだけ小さくすることが
できる。Therefore, as a result, the absolute value of the compressive stress is reduced, and the creep life consumption can be reduced accordingly.
なお第６図において、材質、設計圧力にもよるが、例え
ば、保持時間１００時間で圧縮最大相当応力δｔを１６
蝙−から１５〜〜 に抑えるこ、 とができれば、寿命
消費率φは約０．００００７から約０．００００６にな
り寿命消費を約１４％低減することができる。In Fig. 6, although it depends on the material and design pressure, for example, if the maximum equivalent compressive stress δt is 16 at a holding time of 100 hours,
If it is possible to suppress the loss to 15~~, the lifetime consumption rate φ will go from about 0.00007 to about 0.00006, and the lifetime consumption can be reduced by about 14%.
本発明は実測値な基にボイラ耐圧部に発生する熱応力を
予測する熱応力ピーク予？ｌｌＩ器と、この熱応力ピー
ク予測器からの熱応力ピーク予測値を基に主蒸気圧力を
設定する主蒸気圧力設定器を設け、主蒸気圧力設定器か
らの主蒸気圧力設定値と、主蒸気圧力検出器からの主蒸
気圧力実測値との偏差によってボイラ耐圧部の内圧を高
めるようにしたので、ボイラ起動時に発生する熱応力を
減少して寿命消費を低減することができ、しかもＤＳ８
運転を行なうものにおいては特に有効である。The present invention is a thermal stress peak prediction system that predicts the thermal stress generated in the boiler pressure-resistant part based on actual measured values. A main steam pressure setter that sets the main steam pressure based on the predicted thermal stress peak value from the thermal stress peak predictor is provided. Since the internal pressure of the boiler pressure-resistant section is increased based on the deviation from the actual main steam pressure measured by the pressure detector, it is possible to reduce the thermal stress that occurs when starting the boiler and reduce the life consumption.Moreover, the DS8
This is particularly effective for vehicles that are driven.
第１図は本発明の実施例に係るボイラ昇圧制御装置の概
略系統図、第２図は変圧運転強制貫流ボイラの概略系統
図、第３Ｖ４は出口ヘッダのノズルコーナ部を示す拡大
断面図、第４図はボイラ起動時の発生応力模式図１．第
５図は第４図の応力とひずみの特性曲線図、第６図は圧
縮最大相当応力と寿命消費率の特性曲線図、第７図は起
動時の蒸気圧力、蒸気温度の時間変化を示す特性曲線図
、第８１１！Ｊは熱応力、内圧応力の時間変化？示す特
性曲線図である。
３４・・・タービンバイパス弁、４１・・・燃料ｍｔｍ
弁、４２・・・出口ヘッダ、４３・・・ノズルコーナ部
、４５・・・蒸気温度実測値、４６・・・蒸気圧力検出
器、４７・・・蒸気圧力実測値、４９・・・蒸気流量実
測値、６３・・・熱応力ピーク予測器、６４・・・熱応
力ピーク予測値、６５・・・主蒸気圧力設定器、６６・
・・主蒸気圧力設定値、６７・・・演算器、６８・・・
偏差、７１・・・弁開度調節器。
第２図
第３図
第４図
＠５図
第６図
〃
□寿命清Ｉ卆ψFig. 1 is a schematic system diagram of a boiler boost control device according to an embodiment of the present invention, Fig. 2 is a schematic system diagram of a variable pressure operation forced once-through boiler, No. 3V4 is an enlarged sectional view showing the nozzle corner of the outlet header, and No. 4 Figure 1 is a schematic diagram of the stress generated during boiler startup. Figure 5 is a characteristic curve diagram of stress and strain in Figure 4, Figure 6 is a characteristic curve diagram of maximum compressive equivalent stress and life consumption rate, and Figure 7 is a graph of steam pressure and steam temperature changes over time at startup. Characteristic curve diagram, No. 811! Is J the temporal change in thermal stress or internal pressure stress? FIG. 34...Turbine bypass valve, 41...Fuel mtm
Valve, 42... Outlet header, 43... Nozzle corner section, 45... Steam temperature actual value, 46... Steam pressure detector, 47... Steam pressure actual value, 49... Steam flow rate actual measurement Value, 63... Thermal stress peak predictor, 64... Thermal stress peak predicted value, 65... Main steam pressure setting device, 66.
...Main steam pressure setting value, 67...Calculator, 68...
Deviation, 71...Valve opening adjuster. Figure 2 Figure 3 Figure 4 @ 5 Figure 6
Claims (1)
を基に燃料調節弁、タービンバイパス弁を開、閉する弁
開度調節器を備え、ボイラ起動時の昇圧を制御するもの
において、前記実測値を基にボイラ耐圧部に発生する熱
応力を予測する熱応力ピーク予測器と、この熱応力ピー
ク予測器からの熱応力ピーク予測値を基に主蒸気圧力を
設定する主蒸気圧力設定器を設け、主蒸気圧力設定器か
らの主蒸気圧力設定値と、主蒸気圧力検出器からの主蒸
気圧力実測値との偏差によってボイラ耐圧部の内圧を高
めるようにしたことを特徴とするボイラ昇圧制御装置。The above-mentioned device is equipped with a valve opening controller that opens and closes a fuel control valve and a turbine bypass valve based on actual measured values of steam temperature, steam flow rate, and pressure from a boiler pressure-resistant part, and controls pressure increase at the time of boiler startup. A thermal stress peak predictor that predicts the thermal stress generated in the boiler pressure-resistant part based on actual measurement values, and a main steam pressure setting device that sets the main steam pressure based on the thermal stress peak predicted value from this thermal stress peak predictor. A boiler booster characterized in that the internal pressure of the boiler pressure-resistant part is increased by the deviation between the main steam pressure setting value from the main steam pressure setting device and the main steam pressure actual value from the main steam pressure detector. Control device.
Priority Applications (1)
| Application Number | Priority Date | Filing Date | Title |
|---|---|---|---|
| JP59205499A JPH0646083B2 (en) | 1984-10-02 | 1984-10-02 | Boiler boost controller |
Applications Claiming Priority (1)
| Application Number | Priority Date | Filing Date | Title |
|---|---|---|---|
| JP59205499A JPH0646083B2 (en) | 1984-10-02 | 1984-10-02 | Boiler boost controller |
Publications (2)
| Publication Number | Publication Date |
|---|---|
| JPS6183802A true JPS6183802A (en) | 1986-04-28 |
| JPH0646083B2 JPH0646083B2 (en) | 1994-06-15 |
Family
ID=16507868
Family Applications (1)
| Application Number | Title | Priority Date | Filing Date |
|---|---|---|---|
| JP59205499A Expired - Fee Related JPH0646083B2 (en) | 1984-10-02 | 1984-10-02 | Boiler boost controller |
Country Status (1)
| Country | Link |
|---|---|
| JP (1) | JPH0646083B2 (en) |
Cited By (1)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| JP2011157853A (en) * | 2010-01-29 | 2011-08-18 | Chugoku Electric Power Co Inc:The | Heat recovery device and heat recovery method for turbine in power generation facility |
Citations (1)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| JPS59219604A (en) * | 1983-05-26 | 1984-12-11 | 株式会社日立製作所 | Controller for warm air in steam piping |
-
1984
- 1984-10-02 JP JP59205499A patent/JPH0646083B2/en not_active Expired - Fee Related
Patent Citations (1)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| JPS59219604A (en) * | 1983-05-26 | 1984-12-11 | 株式会社日立製作所 | Controller for warm air in steam piping |
Cited By (1)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| JP2011157853A (en) * | 2010-01-29 | 2011-08-18 | Chugoku Electric Power Co Inc:The | Heat recovery device and heat recovery method for turbine in power generation facility |
Also Published As
| Publication number | Publication date |
|---|---|
| JPH0646083B2 (en) | 1994-06-15 |
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